FINAL REPORT TO WRIGHT AIR DEVELOPMENT CENTER, MATERIALS LABORATORY ON A SURVEY OF THE RELATIONS BETWEEN MICROSTRUCTURE AND ELEVATED-TEMPERATURE PROPERTIES OF FOUR LOW-ALLOYED STEELS AT 700- TO 1200'F By A. I. Rush J. W. Freeman Engineering Research Institute, University of Michigan Project Number: 1903 AIR FORCE CONTRACT NUMBER AF33(038)-13496 RESEARCH AND DEVELOPMENT ORDER NUMBER 615-13 March 31, 1954

FOREWORD This report was prepared by the University of Michigan, under USAF Contract No. AF 33(038)-13496. The contract was initiated under Research and Development Order No. 615-13, "High Temperature Alloys," and was administered under the direction of the Materials Laboratory, Directorate of Research, Wright Air Development Center, with Mr. C. B. Hartley acting as project engineer. ii

A SURVEY OF THE RELATIONS BETWEEN MICROSTRUCTURE AND ELEVATED-TEMPERATURE PROPERTIES OF FOUR LOW-ALLOYED STEELS AT 700- TO 1200'F SUMMARY The relationships between type of microstructure and properties at 700' to 1200'F were surveyed for four low alloyed steels. The steels were SAE 4340, 1.25 Cr - Mo - Si - V ("17-22A"S), 3 Cr - Mo - W - V (H-40), and 13 Cr - Mo - W - V (C-422). Near pure structures were produced by isothermal transformation at a series of temperatures. Martensitic structures were produced by oil quenching. Normalized specimens were also included. Maximum Brinell hardness was kept at 280-320 by tempering the structures which had higher hardness as transformed. The results indicated that bainitic structures had maximum strength over the temperature range. Tempered martensite in general had intermediate to low strengths. Pearlites were relatively weak at low temperatures, but became similar to the bainites at the higher temperatures. There was considerable variation between high and low temperature bainite and between fine and coarse pearlite. Normalized materials apparently have generally high levels of strength because the usual structures developed are predominantly bainite. In most cases, rather wide variations in structure were possible with rather uniform properties. There were, however, usually a predominantly strong and an abnormally weak structure within the generalizations. Alloy content controlled the level of strength for a given structure. Thus, while martensitic structures compared unfavorably to the bainites for SAE 4340 and "17-22A"S, the martensitic structure of the C-422 alloy was superior to the lower alloyed steels at the higher temperature and longer time periods. Reasonably good correlations were developed between the structures and properties of turbine wheels of the four alloys on the basis of the results of the survey. The general results from the survey appear to be useful for general guidance in heat treating alloys for high temperature service. However, the survey is very limited and care should be used in extending the data until all the factors have been investigated. iii

TABLE OF CONTENTS Page INTRODUCTION 1 TEST MATERIALS 2 SELECTION OF MICROSTRUCTURES AND TESTING CONDITIONS 3 Transformation Conditions 3 SAE 4340 and "17-22A"S Steels 5 H-40 Steel 5 C-422 Steel 6 Evaluation of High Temperature Properties of the Various Structures 6 SAE 434- Steel 7 "17-22A."S Steel 7 H-40 Steel 8 C-422 Steel 8 RESULTS 9 SAE 4340 Steel 9't17-22A"S Steel 11 H-40 Steel 12 C-422 Steel 13 Microstructural Changes During Testing 14 CORRELATION OF STRUCTURES AND PROPERTIES OF TURBINE WHEELS 14 SAE 4340 Steel 16 rr17-22A"S Steel 17 H-40 Steel 18 C-422 Steel 19 DISCUSSION 20 Principles of Heat Treatment 20 Relationship Between Type of Structure and Chemical Composition 22 Estimation of Strengths from Microstructures 23 Limitations of Results 24 CONCLUSIONS 25 BIBLIOGRAPHY 26 iv

LIST OF TABLES Table Page I Type Structures, Heat Treatments and Actual Structures for 4340 Steel 27 II Type Structures, Heat Treatments and Actual Structures of a 1. 25 Cr-Mo-S-V ("'17-22ArS) Steel 28 III Type Structures, Heat Treatments and Actual Structures for 3 Cr-Mo-W-V (H-40) Steel 29 IV Rupture, Total Deformation, and Creep Data at 700, 900', 1000', and 1100~F for Isothermally Transformed 4340 Steel 30 V Rupture, Total Deformation, and Creep Data at 700, 900~, 1100 and 1200~F for Isothermally Transformed Structures of a 1. 25 Cr-M-Si-V (' 17-22A"S) Steel 32 VI Rupture, Total Deformation, and Creep Data at 700~, 900', 1100, and 1200'F for Isothermally Transformed H-40 Steel 34 VII Rupture, Total Deformation and Creep Data at 1100~F for Heat Treated Bar Stock of C-422 Steel 35 VIII Rupture, Total Deformation and Creep Strengths at 1000~ and 1100~F for Turbine Wheels and Isothermally Transformed Bar Stock of SAE 4340 Steel 36 IX Relative Strengths of Structures for 4340 Steel 37 X Rupture, Total Deformation and Creep Strengths at 1100~ and 1200~F for Turbine Wheels and Isothermally Transformed Bar Stock of "17-22A"S Steel 38 XI Relative Strengths of Structures for "'17-22A"S Steel 39 v

LIST OF TABLES (Continued) Table Page XII Rupture, Total Deformation and Creep Strengths at 1100~ and 1200'F for Turbine Wheels and Isothermally Transformed Bar Stock of H-40 Steel 40 XIII Rupture, Total Deformation and Creep Strengths at 1100~F for Turbine Wheels and Heat Treated Bar Stock of C-422 Steel 41 XIV Chemical Composition of Forged Turbine Wheels 42 XV Heat Treatments of Forged Turbine Wheels 43 XVI Comparison of Microstructures and Properties of Turbine Wheels with Comparable Structures for Bar Stock of SAE 4340 Steel at 1000~ and 1100'F 45 XVII Comparison of Microstructures and Properties of Turbine Wheels with Comparable Structures for Bar Stock of'"17-ZZA"S Steel at 1100' and 1200'F 46 XVIII Comparison of Microstructures and Properties of Turbine Wheels with Comparable Structures for Bar Stock of H-40 Steel at 1100'F 47 XIX Comparison of Microstructures and Properties of Turbine Wheels with Comparable Structures for Bar Stock of C-422 Steel at 11000F 48 vi

LIST OF ILLUSTRATIONS Figure Page 1 Time-Temperature Transformation Curves for 4340, Austenitized 1550'F, Grain Size 7/8 49 2 Time-Temperature Transformation Curves for Timken "17-22A"S, Austenitized at 1750~F 50 3 Time-Temperature Transformation Curve for H-40, Austenitized at 1950~F 51 4 Time-Temperature Transformation Curve for C-422, Austenitized at 1900'F 52 5 4340 Bar Stock (a) As Transformed to Upper Pearlite and (b) After Creep Testing at 1000~F 53 6 4340 Bar Stock (a) As Transformed to Middle Pearlite and (b) After Creep Testing at 1000~F 54 7 4340 Bar Stock (a) As Transformed to Lower Pearlite and (b) After Creep-Rupture Testing at 1000~F 55 8 4340 Bar Stock (a) As Transformed to Upper Bainite and (b) After Creep Testing at 1000F 56 9 4340 Bar Stock (a) As Transformed to Middle Bainite and (b) After Creep Testing at 1000~F 57 10 4340 Bar Stock (a) As Transforrned To Lower Bainite, (b) As Tempered to 300 BHN, and (c) After Creep Testing at 1000F 58 11 4340 Bar Stock (a) As Oil Quenched, (b) As Tempered to 300 BHN, and (c) After Creep Testing at 1000F 59 12 4340 Bar Stock (a) As Normalized, (b) As Tempered to 300 BHN, and (c) After Creep Testing at 1000~F 60 13 "17-22A"S Bar Stock (a) As Transformed to Upper Pearlite and (b) As Creep-Rupture Tested at 1100F 61 vii

LIST OF ILLUSTRATIONS (Continued) Figure Page 14 11'7-22A"S Bar Stock (a) As Transformed to Middle Pearlite and (b) As Creep-Ruptured Tested at 1100~F 62 15 r,17-22A"S Bar Stock (a) As Transformed to Lower Pearlite, (b) As Tempered to 300 BHN, and (c) After Creep-Rupture Testing at 1100'F 63 16 "17-22A"S Bar Stock (a) As Transformed to Upper Bainite, (b) As Tempered to 300 BHN, and (c) After Creep-Rupture Testing at 1100F 64 17 "17-22A"S Bar Stock (a) As Transformed to Middle Bainite, (b) As Tempered to 300 BHN, and (c) After Creep-Rupture Testing at 1100F 65 18'r17-22Ar'S Bar Stock (a) As Transformed to Lower Bainite, (b) As Tempered to 300 BHN, and (c) After Creep-Rupture Testing at 1100~F 66 19 "17-22A"S Bar Stock (a) As Oil Quenched, (b) As Tempered to 300 BHN, and (c) After Creep-Rupture Testing at 1100F 67 20 "tl7-22A"S Bar Stock (a) As Normalized, (b) As Tempered to 300 BHN, and (c) After Creep-Rupture Testing at 1100F 68 21 H-40 Bar Stock (a) As Transformed to Pearlite and (b) After Rupture Testing at 11000F 69 22 H-40 Bar Stock (a) As Transformed to Bainite, (b) As Tempered to 300 BHN, and (c) After CreepTesting at 11000F 70 23 H-40 Bar Stock (a) As Oil Quenched, (b) As Tempered to 300 BHN, and (c) After Creep-Rupture Testing at 1100~F 71 viii

LIST OF ILLUSTRATIONS (Continued) Figure Page 24 H-40 Bar Stock (a) As Normalized, (b) As Tempered to 300 BHN, and (c) As Creep-Rupture Tested at 1100~F 72 25 C-422 Bar Stock (a) As Oil Quenched, (b) As Tempered to 300 BHN, and (c) After Creep Testing at 1 100F 73 26 C-422 Bar Stock (a) As Normalized, (b) As Tempered to 300 BHN, and (c) After Creep-Rupture Testing at 1100~F 74 27 Comparison of Stress-Rupture Data at 1000' and 1100~F Between Isothermally Transformed Structures and Variously Heat-Treated Turbine Wheels of SAE 4340 Steel 75 28 Comparison of 0. 5 Percent Total Deformation Data at 1000~ and 1100'F Between Isothermally Transformed Structures and Various Heat-Treated Turbine Wheels of SAE 4340 Steel 76 29 Comparison of One Percent Total Deformation Data at 1000~F and 1100~F Between Isothermally Transformed Structures And Variously Heat-Treated Turbine Wheels of SAE 4340 Steel 77 30 Comparison of Stress-Creep Rate Data at 1000~ and 1100F Between Isothermally Transformed Structures and Variously Heat-Treated Turbine Wheels of SAE 4340 Steel 78 31 Relationship Between Properties at 700', 900~, 1000~ and 1100~F of Isothermally Transformed Structures of SAE 4340 Steel and Temperature of Transformation 79 32 Comparison of Stress-Rupture Data at 1100~ and 1200F Between Isothermally Transformed Structures and Variously Heat-Treated Turbine Wheels for "17-22A"S Steel 80 ix

LIST OF ILLUSTRATIONS (Continued) Figure Page 33 Comparison of 0. 5 Percent Total Deformation Data at 11000 and 1200F Between Isothermally Transformed Structures and Variously Heat-Treated Turbine Wheels for "17-22A"S Steel 81 34 Comparison of One Percent Total Deformation Data at 1100 and 1200'F Between Isothermally Transformed Structures and Variously Heat-Treated Turbine Wheels for "17-2ZA"S Steel 82 35 Comparison of Stress-Creep Rate Data at 1100~ and 1200'F Between Isothermally-Transformed Structures and Variously Heat-Treated Turbine Wheels for 17-22A"S Steel 83 36 Relationship Between Properties at 700~, 900', 1100~, and 1200'F of Isothermally Transformed Structures of "17-22A"S Steel and Temperature of Transformation 84 37 Comparison of Stress-Rupture Data at 1100~ and 1200F Between Isothermally Transformed Structures and Variously Heat-Treated Turbine Wheels for H-40 Steel 85 38 Comparison of 0. 5 Percent Total Deformation Data at 1100' and 1200'F Between Isothermally Transformed Structures and an Oil Quenched and Tempered Turbine Wheel of H-40 Steel 86 39 Comparison of One Percent Total Deformation Data at 1100~ and 1200'F Between Isothermally Transformed Structures and an Oil Quenched Turbine Wheel of H-40 Steel 87 40 Comparison of Stress-Creep Rate Data at 1100~F Between Isothermally Transformed Structures and an Oil Quenched and Tempered Turbine Wheel of H-40 Steel 88 x

LIST OF ILLUSTRATIONS (Continued) Figure Page 41 Comparison of Stress-Rupture Data at 1100~F Between Normalized and Oil Quenched Bar Stock and Variously Heat-Treated Turbine Wheels of C-422 Steels 89 42 Comparison of 1. 0 and 0. 5 Percent Total Deformation Data at 1100~F Between Normalized and Oil Quenched Bar Stock and an Oil Quenched and Tempered Turbine Wheel of C-422 Steel 90 43 Comparison of Stress-Creep Rate Data at 1100~F Between Normalized and Oil Quenched Bar Stock and an Oil Quenched and Tempered Turbine Wheel of C-422 Steel 91 44 Typical Microstructures of 4340 Disk No. 1 (Normalized) 92 45 Typical Microstructures of 4340 Disk No. 3 (Oil Quenched and Tempered) 93 46 Typical Microstructure of 4340 Disk No. 4 (Interrupted-Quenched and Tempered) 94 47 Microstructures of Ruptured Specimens of 4340 Disk Nos. 1, 3, and 4 95 48 Typical Microstructures of "17-22A"S Disk No. 1 (Normalized and Tempered) 96 49 Typical Microstructures of "17-22A"S Disk No. 3 (Oil Quenched and Tempered) 97 50 Typical Microstructures of t'17-22A"S Disk No. 4 (Interrupted-Quenched and Tempered) 98 51 Typical Microstructures of Ruptured Specimens of "17-22A"S Disk Nos. 1, 3, and 4 99 52 Typical Microstructures of As-Received H-40 Disk No. 1 (Normalized and Tempered) 100 xi

LIST OF ILLUSTRATIONS (Continued) Figure Page 53 Typical Microstructures of As-Received H-40 Disk No. 3 (Oil Quenched and Tempered) 101 54 Typical Microstructures of As-Received H-40 Disk No. 4 (Interrupted-Quenched and Tempered) 102 55 Microstructures of H-40 Disk Nos. 1, 3, and 4 After Retempering 4 Hours at 1250'F 103 56 Microstructures of Ruptured Specimens of AsReceived H-40 Disk Nos. 1, 3, and 4 104 57 Microstructures of Ruptured Specimens of Retempered H-40 Disk Nos. 1, 3, and 4 105 58 Typical Microstructures of C-422 Disk No. 1 (Normalized and Tempered) 106 59 Typical Microstructures of C-422 Disk No. 4 (Oil Quenched and Tempered) 107 60 Microstructures of Ruptured Specimens of C-422 Disks Nos. 1 and 4 108 xii

INTRODUC TION Normal heat-treatment of medium carbon low alloyed steels can result in microstructures ranging from martensite through the bainites and pearlites, depending upon the section sizes and cooling conditions. A survey has been carried out to relate the possible structures to rupture and creep properties at temperatures from 700~ to 1200~F. Four steels were used: 4340, 1.25 Cr - 0. 5 Mo - 0.75 Si - 0.25 V ("17-22A"S), 3 Cr - 0.5 Mo - 0.5 W - 0.8 V (H-40), and 13 Cr - 1 Mo - 0.8 W - 0. 25 V (C-422). The relationships obtained were extended to correlate the structures and properties of normalized bar stock and turbine wheel forgings of the same alloys, The structures developed in such steels depend on their transformation characteristics and cooling rates during heat-treatment. It has been known that the properties at elevated temperatures vary with the structures, but the relationships have not been defined. For this reason, an investigation was undertaken to survey the relative creep and rupture strengths of microstructures ranging from martensite through the bainites and pearlites. Nearly "pure structures", produced by isothermal transformation at a number of temperatures, were evaluated by a limited number of creep and rupture tests. The information obtained was checked by correlating the structures and properties with those of normalized (air quenched) bar stock. The structure of turbine wheel forgings of the same alloys were determined and correlated with previously reported properties (Ref. 1). Very little information is available relating microstructures of such steels to properties at high temperatures. The usual superior creep strength of the normalized structure in comparison to martensite produced by liquid quenching when both were tempered to the same hardness has been long recognized. It has been noted that the normalized structure with high strength usually had a predominantly bainitic structure. Other studies had shown that above some limiting temperature pearlitic structures became superior. These generalities were very difficult to use in practice. A rather wide range in structures is possible within the general classifications of pearlite and bainite. Secondly, the more common commercial heat-treatments involve continuous cooling transformation which may produce mixed structures. One of the major objectives of the investigation was to obtain information that might lead to the increased use of low-alloy steels for applications 1

heretofore requiring high-alloy strategic materials. Creep and rupture properties can be the controlling factors in the use of low-alloyed hardenable steels over the temperature range of 700' to 1200~F. There are a number of applications or possible applications for such materials in jet engines for aircraft within this temperature range. Increasing air temperatures in compressors are leading to consideration of more use of such materials. At least one jet engine uses alloys of the type studied for turbine wheels. Such alloys require only small amounts of such scarce elements as nickel, chromium, and molybdenum, and no columbium or cobalt. Their fabrication characteristics are far superior to high alloyed austenitic steels and super alloys. Both of these characteristics are of considerable strategic importance. Information relating microstructure to properties at elevated temperatures has a number of applications. The metallurgist can use such information to select the best conditions and equipment for heat-treatment of a specific section size. Secondly, it would enable proper decisions regarding the usual variations in structure to be expected in practice. It is often difficult to obtain equipment for heat-treatment which will produce ideal structures. Variation in section size in any specific part requires compromises in heat-treatment for best overall properties. Furthermore, the variation in response to heat-treatment normally encountered in practice, and to be expected from the usual heat-to-heat transformation characteristics, as well as plant procedure, requires that good basic information be available for the establishment of sound inspection control. TEST MATERIALS The chemical compositions of the bar stock material used for the study of the properties of isothermally transformed structures and structures obtained by conventional normalizing and quenching treatments were as follows: Steel Heat C Mn Si Cr Ni Mo V W Cu 4340 19053 0.40 0. 70 0.30 0.78 1.75 0.26 -- -- 0.12 "17-22A"S 24797 0.30 0. 63 0. 60 1.25 0.25 0.52 0. 25 -- 0. 10 "17-22A"S 10420 0. 29 0. 61 0.67 1.30 0. 18 0.47 0. 26 H-40 K-2509 0.29 0. 48 0. 26 3. 05 0.49 0.49 0. 85 0. 55 0. 15 C-422 W-3561 0.23 0.81 0. 16 13. 19 0.65 1.03 0.25 0.84 2

Since the amount of work originally contemplated was enlarged during the course of the investigation, it was necessary to obtain additional bar stock. Additional stock of the 4340 steel was obtained from the same heat as originally used, but it was necessary, however, to accept additional stock from another heat of "17-2ZA"S. The original supply of H-40 and C-422 bar stock was sufficient for the investigation. The chemical composition and heat treatments of the turbine wheels whose microstructures and properties were correlated as part of this investigation have been outlined previously in Reference 1. It was possible to obtain bar stock from the same heats as the turbine wheels for the H-40 and C-422 steels, but it was necessary to accept different heats for the SAE 4340 and "17-22A"S bar stock. SELECTION OF MICROSTRUCTURES AND TESTING CONDITIONS The initial step was to establish transformation conditions for the possible structures in the four steels, prepare specimens with structures to survey the range in structures, and to select suitable survey test conditions. Transformation Conditions The initial step in the study was to obtain isothermal transformation diagrams for the four steels. Inasmuch as several diagrams have been published for SAE 4340 steel, it was not believed necessary to establish one for this material. The diagram published by the United States Steel Company (Ref. 2) was used for this study and is reproduced in Figure 1. Similar diagrams were determined for the "17-22A"S, H-40, and C-422 steels, as shown in Figures 2, 3, and 4. Following the determination of the isothermal transformation diagrams, time and temperatures of transformation were selected to obtain certain idealized microstructures which would cover the range of structures possible. The treatments and resulting structures are outlined in Tables I through III. The names of the idealized structures are a convenient way of identifying for discussion purposes the treatments and structures used. It is important to recognize, however, as shown in the tables, that in some cases the actual structures deviated from the idealized structure. Photomicrographs illustrating typical microstructures are shown in Figures 5 through 26 for the four steels. 3

The major reason for the variations between idealized aim structures and the actual structures was the time for complete transformation, Partial transformation to the desired structure could be obtained, but the time to complete the transformation would have been excessive. For example, "upper bainite" in the 4340 steel was only 70 percent bainite with 30 percent martensite after transforming 28 hours at 850~F. The transformation diagram, however, indicates that times in excess of a week would be required to obtain complete transformation. When considerably longer times than those used would not have resulted in appreciably greater transformation, it was deemed advisable to accept the structures most closely resembling those which might be obtained in practice. Furthermore, prolonged transformation times might have resulted in tempering of the first formed transformation products. Both standard 0. 505- and 0. 250-inch test bars were used. The 0. 505-inch specimens were employed for the normalized and oil-quenched bars and for transformations in the pearlitic range. For transformation in the bainitic range, the 0. 250-inch specimens were used to assure rapid cooling to the isotherm so that transformation could not occur at higher temperatures. It was necessary also to use 0. 250-inch specimens for all structures when the high stresses involved at the 700~ and 900~F testing temperatures exceeded the capacity of the testing units for the larger diameter specimens. Prior to heat treating, the bar stock was rough machined to cylindrical bars 0. 8 and 0. 4 inches in diameter and final machining was performed after all heat treating operations had been completed. Austenitizing of the bars was performed in electrical resistance furnaces for the lower temperatures and in a gas fired muffle furnace for temperatures above 1800~F. To assure uniform temperatures in the salt baths used for isothermal transformations, agitation was accomplished by means of a stirrer driven by an air motor. An austenitizing temperature of 1750F was used for the 4340 and "'17-22A"S materials, whereas 1950~ and 1900~F were employed for the H-40 and C-422 steels, respectively. The selection of these temperatures was based on their use for the heat treatment of the turbine wheels, and, with the exception of the 1750~F temperature for the 4340 material, were those most commonly used for the subject materials. The 1750~F austenitizing temperature for the 4340 was somewhat higher than normally used, but can be justified on the basis of the large section sizes involved in the turbine wheels. The aim hardness was 300 Brinell with the range of 280 to 320 being considered acceptable. When the as-transformed or heat-treated hardnesses 4

exceeded 320 BHN, tempering was used to reduce the hardness to about 300 Brinell. The microstructures after tempering and after prolonged testing at 1000~F for 4340 and 1100~F for the other alloys are also illustrated in the same figures as the as-transformed structures, The transformation temperatures were chosen in the following manner. SAE 4340 and "17-22A"'S Steels The highest temperature was chosen in the upper limit of the pearlitic nose of the curve such that transformation would occur in a reasonable time, and the resulting structure was designated "upper pearlite." The lower temperature limit below the pearlite nose of the curve where only pearlite would form was chosen for the "lower pearlite" structure. The "middle pearlite"r structure was obtained by transformation -at an intermediate temperature. The same procedure was used for choosing transformation temperatures in the bainitic region. Additional microstructures were obtained by normalizing and tempering and oil quenching and tempering according to the schedule shown in Tables I and II. These treatments resulted in a mixed martensiticbainitic and a completely martensitic microstructure, respectively. Photomicrographs of the resulting microstructures are shown in Figures 5 through 12 for the SAE 4340 material and in Figures 13 through 20 for "' 17-22A"S. Complete transformation to the desired structures was obtained except for the "upper bainitic" and "middle bainitic" structures. For 4340 only 70 percent completion was secured for the upper bainitic structure and for "17-22A"S, 60 and 97 percent completion were obtained for the upper and middle bainites respectively. H-40 Steel All transformations in the upper nose of the H-40 diagram resulted in a fine carbide precipitate. Therefore, only one transformation temperature was chosen and the resulting structure referred to as "pearlite. " Only one transformation product in the bainitic region was studied since the temperature range in which the bainitic structures could be obtained within reasonable times was quite narrow. 5

In addition, as for 4340 and "17-22A"S,the elevated temperature properties were obtained for normalized and tempered and oil-quenched and tempered bar stock. Photomicrographs of the resulting structures are shown in Figures 21 through 24, and Table III presents the pertinent data regarding these structures. C-422 Steel As shown in Figure 4, the only transformation which began in a reasonable time period for the C-422 material was a grain boundary carbide precipitate, and this transformation apparently was not complete in a very long time. Consequently, the C-422 bar stock was investigated in the normalized and tempered and quenched and tempered conditions only. Both of these treatments produced complete martensitic structures, as shown in Figures 25 and 26. Evaluation of the High-Temperature Properties of the Various Structures The general objective of the tests was to determine the relative strengths of the various structures by survey tests in the temperature range of 700~ to 1200~F. At 700' and 900~F, the evaluation was mainly on the basis of creep and total deformation characteristics, the controlling factors at those temperatures. Stress-rupture and total deformation in 1000 hours were the more useful criteria at 1000~ and 1100~F, and short-time rupture data were the basis of comparison at the higher temperatures, 1100~ and 1200~F, depending upon the material. In each case, as few tests as possible to obtain an indication of strength were used. This alone led to a rather extensive testing program. Furthermore, it was considered advisable to survey the magnitude of the effects before undertaking extensive testing of individual structures. The survey tests employed for the different materials are outlined below. 6

SAE 4340 Steel At 700~F, comparisons were based on a single stress of 90, 000 psi. It resulted in total deformations in 1000 hours of about 1. 0 percent for the stronger structures. No attempts were made to obtain stress-rupture data since at this temperature the stresses would have to be well above the yield strengths. At 900~F, comparisons were based on two stresses, 55, 000 psi and 40, 000 psi. The former was selected to yield for the stronger structures approximately 1000-hour stress-rupture tests, whereas the latter was expected to give total deformation values in the order of 1. 0 percent in 1000 hours. Although, in general, creep and total deformation values are of more interest at this temperature, it was believed that the low strength of the 4340 material at high temperatures made a knowledge of its rupture properties at 9000F useful. The most extensive data were obtained for 4340 at 1000~F since this is about the upper limit of useful application of this steel for relatively long periods, and because the most extensive data on the turbine wheels were obtained at this temperature. In general, two to four tests were run on each microstructure to obtain creep and total deformation data, as well as to establish the stress-rupture curves for the stronger microstructures. At 1100~F, two stresses were employed -- 18,000 psi to establish the short-time rupture strengths and 4, 500 psi to obtain creep and total deformation data. I'17-22A"S Steel In general, the testing procedures for "17-22A"S were similar to those outlined above for 4340 steel. However, the wide spread in strengths of the different microstructures at 7000F required the use of two stresses to obtain a better evaluation of the strengths. The initial stress of 115, 000 psi did not prove to be very useful in evaluating the structures at 700~F. In most cases, this stress was too high, as evidenced by the rupture of most of the specimens in rather short-time periods. Since at 700~F, yield strengths govern the maximum stress which can be used, additional tests were conducted using a stress between the proportional limit and 0. 2-percent offset yield strength (approximately the 0. 05-percent offset yield strength) as the sorting stress. Because of the flat slope of the stress - creep rate curve at 7000F, this method of selecting stresses did not result in exactly comparable total deformation and creep data, but it was believed that a better evaluation would 7

be obtained on the basis of behavior at the various yield stresses than at a fixed stress which would have been both above and below the yield strength of the various structures. At 900~F, one stress, 70, 000 psi, gave either rather long time rupture data or satisfactory total deformation data. For this steel, the most extensive data were obtained at 1100~F, the temperature for which the most data were available for the turbine wheels. Several tests were run on each material to obtain stress-rupture, total deformation, and creep data. At 1200~F, two stress levels, 14, 000 and 7, 500 psi, were employed to obtain short-time stress-rupture data, as well as a limited amount of longer time rupture and total deformation data. H-40 Steel A single stress was employed at both 7000 and 900~F, 90, 000 and 65, 000 psi, respectively. These stresses produced creep and total deformation data for the stronger structures and rupture data for the weaker structures. As for the I"17-22A'S material, rather extensive data were obtained at 1100F. At 1200F, the testing was limited to short-time stress-rupture data at a single stress, 25, 000 psi. C-422 Steel As noted previously, isothermally transformed structures were not obtained for the C-422 material. Because of its higher alloy content and less probable use at lower temperatures, testing of the normalized and oil-quenched bar stock was limited to 1100~F. The stress-rupture curve was established by three tests on the normalized material, and a single stress test estimated to give 1. 0 percent total deformation in 1000 hours was run for the oil-quenched bar stock. 8

RESULTS As indicated in the previous section describing the procedures employed, creep rate and total deformation data were obtained at the lower temperatures, 700~ and 900~F; stress-rupture, creep rate, and total deformation at the intermediate temperatures, 1000~ and 1100F; and at the higher temperatures, 1100' and 1200~F, depending upon the material, emphasis was placed on the short-time rupture data. The complete test data are presented for all four steels in Tables IV through VII. Because of the survey nature of the data, the conventional stress-creep rate, stress-rupture time, and stress-total deformation time curves could not be prepared. However, as will be discussed later, the test data are presented in graphical form, along with the turbine wheel data for those temperatures where complete curves were available for the wheels. SAE 4340 Steel The test data from the survey of the relative strengths of the structures are given in Table IV. Table VII[and Figures 27 through 30 summarize the strength values obtained from these data. In order to show the relative strengths more clearly, Table IX and Figure 31 have been prepared. The important trends from this data were: 1. The bainites had the highest strength over the entire temperature range for the criteria of Table IX. 2. Maximum strength shifted from lower to middle to upper bainite with increasing temperature. 3. The mixed bainitic and martensitic structure resulting from normalizing the bar stock had strengths approximately the same as the strongest bainite. From a structural analysis viewpoint, the normalized structure most closely approached upper bainite. At the lower temperatures it tended to be stronger and at the higher temperatures somewhat weaker than upper bainite. 4. At 700 and 900 ~F, the indications are that substantially increased strength can be obtained by heat treating to fine or medium bainites. The difference between structures tends nto become less with increasing temperature, however, so that the penalty for structural variation is not so great, 9

5. Tempered martensite appeared to retain about the same relative strength to the bainites at all temperatures, being somewhat weaker. At 1000' and 1100~F, however, the pearlites tended to compare more favorably with the bainites and actually be stronger than the martensite. Careful inspection of the data shows that at 1000~ and 1100~F, the martensite tended to become the weakest of all structures for limited deformation and prolonged time periods. 6. As would be expected, there were shifts in relative positions between the structures with both test temperature and criterion of strength. The pearlites tended to compare more favorably the higher the temperature, the longer the time period, and the smaller the total deformation. This was particularly true for upper pearlite, which tended to have high strength at limited deformations at 1000~ and 11000F, but did not compare as well on the basis of rupture strength. The test stresses being above the yield strength of the pearlites at 700~ and 900~F certainly contributed to their poor showing. 7. It is perhaps significant that there was a tendency for a shift in relative strengths of pearlites with increasing test temperature from lower to upper pearlite, as was the case for the bainites. 8. The significance of the indicated relative strengths of the structures at 700~ and 900~F is somewhat difficult to estimate. The limited number of tests did not permit establishment of stresses for rupture or total deformation in a given time period. Comparisons based on time for fracture or to reach a given deformation, or the creep rate, at a fixed stress often exaggerate differences which might be rather small insofar as the influence on the stress for a given strength is concerned. 9. The ductility data from the rupture tests is rather meager for drawing definite conclusions. Review of the data in Table IV indicates the following: (a) At 900~F, elongations decrease very rapidly with time for fracture. When this influence of fracture time is taken into consideration, the pearlites gave at least as low, if not lower, ductility than the bainites. There is a suggestion that lower bainite and the normalized structure retained the best ductility. (b) At 1000~F, the pearlitic and oil-quenched samples tended to have slightly better ductility than the bainitic and normalized samples. (c) At 1100~F, the meager data show no outstanding difference beyond the suggestion that upper pearlite and the oil-quenched material had slightly better ductility. 10

"'17- 2ZA"S Steel The individual test data for the survey of "17-22A"S at 700~, 900~, 1100~, and 1200dF are given in Table V, and the strength values obtained from these data are summarized in Table X and Figures 32 through 35. Table XI and Figure 36 have been prepared to show the relative strengths of the structures more clearly. The shift in structures for optimum strength was not as consistent as for 4340 steel. There appear to be at least three factors influencing the relations between structures and properties which complicate definite conclusions as to optimum structures. The margin between a number of structures was rather small and experimental variations could therefore affect the precise order of strengths. Two heats of steel were used for test specimens. Both heats had essentially the same time-temperature-transformation curves. However, Heat 24797 tended to give higher hardness, particularly in the pearlitic region, than Heat 10420. The latter heat had noticeably more ferrite than the former. This, however, did not seem to account for all the difference in hardness and considerable experience with the alloy suggests that there were in addition secondary hardening differences between the heats not reflected in the microstructures. Because creep resistance appears to be closely related to secondary hardening, this may have been a factor not readily apparent in test performance. With these restrictions in mind, the data appear to indicate the following trends: 1. The bainites showed the highest strengths for all criteria of Table XI for the temperature range of 700' to 11000F. The maximum strength shifted from middle bainite at 7000 and 900~F to lower bainite at 1100~F, as indicated in Figure 36. 2. The maximum strength at 12000F was shown by the upper pearlitic structure. 3. The mixed bainitic and martensitic structure obtained by normalizing bar stock had strengths approximately equal to the best bainite at 1100~F and best pearlite at 1200~F. At 700' and 900~F, the mixed structure was slightly weaker than the middle bainitic structures. From a microstructural viewpoint, the normalized structure most closely resembled the middle bainitic structure, except that the former contained somewhat more martensite. 11

4. The pearlitic structures were surprisingly strong over the entire range of temperature. Although the upper pearlitic structure was the weakest at 700~ and 900~F, it showed considerable improvement at 1100~F, and was the strongest at 12000F. The middle pearlitic structure was only slightly lower than the bainitic and martensitic structures at 700~F and gave good rupture strength at 900F. At 1100' and 1200"F, where the range in strengths was quite narrow, the middle pearlite was only slightly inferior to the best structures, The lower pearlite tended to show intermediate to low strengths over the entire temperature range. 5. The relative strength of the martensitic structure tended to decrease with increasing testing temperature. At 900~F, the martensitic structure gave creep rates similar to the best bainitic structure, but at 1200?F it revealed the lowest 100-hour rupture strength. 6. Comparison of the elongation values at fracture, shown in Table V, indicates the following: (a) Good ductility was obtained at 700' and 900~F, and what data are available at longer time periods at 900~F show little decrease in elongation. (b) The elongation at 1100~F tends to be low and decreases with increasing time. The rather sparse data indicate best ductility for fracture in short time periods for the upper pearlite and martensitic structures, whereas the lower pearlite gave the best long time elongations. (c) Relatively low elongations are shown for short time periods at 1200~F, but the deformation increases with increasing time. (d) The magnitude of the ductility seems to be independent of the structure. H-40 Steel Table VI presents the individual test data for the survey of relative strengths and Table XII and Figures 37 through 40 summarize the strength values obtained from these data. 12

The trends indicated by these data were as follows: 1. The bainitic structure exhibited properties nearly equal or superior to the other structures over the temperature range of 700~ to 1100~F. At 700~ and 900~F, the bainitic structure gave the best properties on the basis of creep and total deformation data. At 1100~F, the bainitic structure was somewhat weaker than the normalized structure on the basis of creep and total deformation strengths, even though it exhibited slightly better rupture strengths. 2. The pearlitic structure had properties slightly better than those for the other treatments at 12000F, as indicated by short-time rupture and total deformation data. 3. The martensitic structure gave properties very similar to the mixed structure obtained by normalizing over the entire temperature range with the following exceptions: (a) The martensitic structure was slightly weaker at 11000F on the basis of creep and total deformation data. (b) At 1200~F, the martensitic structure was the weakest of all treatments, although the difference was relatively small. 4. Good elongation to fracture was obtained for all conditions with the exception of the normalized structure which was quite brittle at 11000F. At 1100~F, only one specimen fractured in the reduced section and three test bars failed either at the shoulder radius or in the threaded end with brittle type fractures. The martensitic structure tended to show the greatest ductility at all temperatures of testing. C-422 Steel The individual test data are presented in Table VII and the relative strengths are summarized in Table XIII and the graphs of Figures 41 through 43. The limited data obtained for this steel indicate that the properties of the oil quenched and normalized bar stock appeared to be nearly identical, as might have been expected from the similar microstructures. 13

Microstructural Changes during Testing The microstructural changes occurring during testing and illustrated in Figures 5 through 26 were of the order to be expected. Little or no change in structure or hardness was observed for the upper and middle pearlitic bar stock. However, the lower pearlitic structure of both the 4340 and I17-22A"S revealed considerable spheroidization during testing at 10000 and 1100~F, respectively. These changes were reflected in both the considerable decrease in hardness during testing, Figures 5 and 15, and in the low high-temperature properties observed for this structure. In general, the bainitic and martensitic structures showed the normal amount of tempering to be expected from testing at 1000~ to 1100~F. The higher alloyed steels indicated less tempering of the microstructure and a greater retention of hardness during testing than the lower alloy steels. CORRELATION OF STRUCTURES AND PROPERTIES OF TURBINE WHEELS A previous report (Ref. 1) presented the results of a survey of the rupture, total deformation, and creep properties of forged turbine wheels of the same steels used for the previously discussed survey of the high-temperature properties of microstructures. The chemical composition and heat treatments of these wheels are reproduced in Tables XIV and XV. The properties obtained from the wheels are summarized in Tables XVI through XIX and Figures 44 through 60. Three heat treatments were used in the wheel testing program. Separate wheels of each alloy were normalized, oil quenched, and "isothermally transformed" from the same austenitizing temperature used in the bar stock studies. The isothermal treatment consisted of quenching in water until the wheel became black, removing from the water until the glow returned from interior heat, and repeating the cycle until the glow did not return. The wheels were then placed in a furnace at 700~F for 8 hours. This was omitted for C-422 alloy due to lack of transformation at intermediate temperatures. The properties obtained are representative of those resulting from the structures established 14

by these treatments of a contour forging 19-1/2 inches in diameter by approximately 3-3/8 inches thick at the rim and 4-5/8 inches thick at the center with an integral stub shaft and boss at the center. As part of the present investigation, the microstructures of the wheels were carefully established. Photomicrographs were taken to show representative structures near the rim, at the center, and midway between the two. These structures are shown by the following figures: 1. SAE 4340 steel - Figures 44, 45, 46, and 47. 2. "17-22A'S steel - Figures 48, 49, 50, and 51. 3. H-40 Steel - Figures 52 through 57. As originally received, the H-40 wheels were found to be too hard and were subsequently retempered. The microstructural analysis was carried out on the as-received material. Figure 55 shows that the retempering did not noticeably change the microstructure. 4. C-422 Steel - Figures 58, 59, and 60. In each case, photomicrographs were included to show typical structures after prolonged testing at the temperatures where the most extensive testing was carried out on the wheels, 1000~F for SAE 4340 and 1100~F for the other three steels. Samples were examined at each location to determine structural variation through the thickness of the disks. Actually, there was very little variation between the surface and center at the three locations, although considerable variation was observed between rim and hub areas in some instances. The photographs were actually taken at a location midway between the surface and central plane of the wheel and are considered to be representative of those existing at the locations of the various test specimens. The photographs of the structure at the position midway between the rim and hub are most representative of the radial specimens used to establish the stress-rupture, total deformation, and creep curves for the wheels. The rim structures are representative of those existing at the location of the tangential check tests taken at the rim. The structure at the central hub area is representative of that of some of the room temperature tensile tests and of check tests run to determine the stressrupture properties of that area. In general, the correlation between the properties of the turbine wheels and their microstructures appears to be rather good. In some instances, the degree of correlation may be obscured by misinterpretation as to the microstructure of the turbine wheels. All turbine wheels, except the normalized 4340 15

wheel, were tempered prior to examination. Tempering tended to obscure the basic microstructure and therefore uncertainty existed in some cases as to the true structure. For example, it is rather difficult to distinguish between the various bainites in the tempered condition, as well as between tempered lower bainite and tempered martensite. Furthermore, the structures of the turbine wheels were formed upon continuous cooling transformation and thus the microstructures might be expected to consist of several components. SAE 4340 Steel The microstructure of the normalized wheel, Figure 44, consisted principally of bainite with moderate amounts of untempered martensite. Greater amounts of martensite were present in the center sections of the wheel, but this apparent anomaly may be attributed to the greater retention of the cast structure and accompanying segregation in the center portions of the wheels, Both the microscopic and macroscopic examination of the wheels indicated less hot working in the center sections. The predominant bainitic structure away from the center appeared to be quite similar to that obtained for the upper bainitic and normalized bar stock, The upper bainitic bar stock had an untempered-bainitic martensitic structure similar to the normalized wheel. The normalized bar stock also was similar, except that it had been tempered. Table XVI and Figures 27 through 30 show that these observations of comparative microstructure appear to agree with the observed high temperature properties. The major difference in properties between the wheel and bar stock structures was the high strength at short time periods for limited deformations shown by the wheel and not indicated by the bar stock structures. In this respect, the normalized bar stock appeared to agree with the turbine wheel data slightly better than did the upper bainitic structure. At about 1000 hours, the bar stock structures gave about the same strength for limited deformations. For some reason, the stress-time curves had much less slope for the bar stock than for the wheels as a result of less creep resistance at high stresses. The relationships existing between the properties of the interruptedquenched wheel and the bar stock materials were similar to those observed for the normalized wheel. This agreement in properties appears to be in accordance with the similarity of structures between the interrupted-quenched and normalized wheels. The photomicrographs of Figures 44 and 46 indicate that 16

the structures of the two wheels were probably similar except for tempering. It was believed that any differences were quickly eliminated during heating for testing. The structure of the oil-quenched wheel appeared to be a uniformly tempered martensite similar to that of the oil-quenched bar stock, Figures 11 and 45. The properties of the oil-quenched wheel and bar stock appeared to be of the same order, but some differences were noted. The short-time rupture strength of the bar stock was slightly lower and the 1000-hour strength slightly higher than for the wheel. Also, the bar stock showed better strength for limited deformation at 1000 hours. Thus, the bar stock material did not exhibit the break in the stress-time curves shown by the wheel material. Perhaps these differences were the result of the different heat treating conditions. The oil-quenched wheel was quenched from 1550~F and tempered an unknown time at 1050*F as compared to 1750F for the bar stock, followed by a temper of 10 hours at 1100~F. The higher tempering temperature for the bar stock may have resulted in a more stable structure that gave higher properties at long time periods. "17-2 2A'S Steel Examination of the microstructure of the normalized wheel revealed a tempered bainitic-ferritic structure near the rim and a tempered pearliticferritic structure containing patches of bainite in the hub area as shown in Figure 48. The bainite in the center areas appeared to be the result of local inhomogeneity resulting in alteration of local transformation characteristics, Because of the mixed nature of the structure, it was not strictly comparable to any of the isothermally transformed structures of the bar stock, but with the exception of the bainitic areas it most closely resembled the middle and lower pearlitic structures. Although extensive data were not obtained for this wheel because of its inferior properties, the available data shown in Table XVII and Figures 32 through 35 indicate that the properties of the pearlitic bar stock materials were generally quite similar to the wheel. The original microstructure of the oil-quenched wheel was difficult to ascertain in the tempered condition. The structure shown in Figure 49 appeared to be a mixture of tempered bainite and martensite, but this conclusion is uncertain because of the similarity in appearance of martensite and lower bainite when both have been tempered. Actually, the structure of the wheel 17

seemed to be more nearly like that of the middle bainitic bar stock structure, Figure 17, except that the wheel structure appeared to be more highly tempered. However, as shown in Table XVII and Figures 32 through 35, the properties of the wheel did not agree quite as well with the middle bainitic structure as with the lower bainite and tempered bainitic-martensitic structure of the normalized bar. The middle bainitic structure had slightly lower properties than the wheel, particularly for limited deformation in 100 hours and for creep, whereas the lower bainitic and normalized structures had properties of the same order for all criteria. This correlation appears to corroborate the initial statement that the structure was probably tempered bainite and martensite, but that considerable lower bainite might have been present. The interrupted-quenched wheel appeared to be tempered martensite or low temperature bainite at the rim and tempered upper or middle bainite, with possible patches of martensite, in the hub areas, Figure 50. As previously mentioned, however, the initial structure is difficult to determine accurately in the tempered condition. Although little data were available for the interruptedquenched wheel, Table XVII and Figures 32 through 35 indicate that its properties were quite similar to the oil-quenched wheel and to the lower bainitic and normalized bars. H-40 Steel As mentioned previously, little difference in properties was observed for the three H-40 steel wheels. Examination of Figures 52, 53, and 54 reveals that there was also little or no difference in microstructure. All three wheels appeared to have tempered bainitic-martensitic structures. In the as-received condition, all three wheels exhibited hardness values above the range of 280 to 320 Brinell desired and therefore coupons cut from the wheels were retempered to obtain the desired hardness. The microstructures of Figure 55 indicate that retempering caused little or no change in structure, although the hardness was reduced considerably. Comparison of the wheel structures with those of the bar stock indicate that the bainitic structure most closely resembled those of the wheels, except for grain size. In all cases, the grain size of the wheels was considerably coarser than that of the bar stock. Comparison of properties, Table XVIII and Figures 37 through 40, indicated rather good agreement between the wheels and the bainitic bar stock, insofar as rupture strength was concerned, but the bar stock gave total deformation and creep strengths considerably lower than the oil-quenched wheel, total deformation and creep data not being obtained for the other wheels. However, although the structure of the normalized bar 18

stock did not agree with the wheel structures as well as the bainitic material, its properties gave better agreement insofar as total deformation and creep data were concerned. It would appear that the higher total deformation and creep strengths and better short-time rupture strength of the wheels could be attributed to their coarser structure, although such a conclusion would have to be corroborated by tests. C-422 Steel The microstructures of both C-422 wheels were tempered martensite and appeared to differ mainly in that the oil-quenched wheel appeared to be more highly tempered. However, the structures seem to be somewhat anomalous in that the rim structure of the oil-quenched wheel appears to be more nearly like the normalized wheel than does the center portion, Figures 58 and 59. It might be expected that the slower cooling rate at the center of the oil-quenched wheel would result in a structure similar to the normalized wheel. On the other hand, the oil-quenched wheel showed greater amounts of delta ferrite in the center sections than was observed for the normalized wheel. Apparently, the delta ferrite was associated with the retained dendritic structure of the ingot and the accompanying segregation of alloying elements. The conclusion that the structures differed mainly in the degree of tempering seems to be substantiated by the fact that the structures were quite similar after prolonged testing as shown in Figure 60. The microstructures of the oil-quenched and normalized bar stock were nearly identical and quite similar to the wheel structures, except that they appeared to be more highly tempered and did not show any delta ferrite. As shown in Table XIX and Figures 41 through 43, the normalized bar stock properties were almost identical with those of the oil-quenched wheel, and the limited data for the oil-quenched bar indicated similar agreement. However, for some reason not explained by the data, the normalized wheel gave properties somewhat lower than the oil-quenched wheel and both bar stock treatments. 19

DISCUSSION The principal purpose of the work reported herein was to survey the relationships between high-temperature properties and microstructures of low alloy steels. In particular, it was desired to determine the relationships between temperature of transformation and elevated temperature properties over a range of testing temperatures, and whether a particular structure exhibited superior properties at one or all temperatures. A secondary purpose was to apply the results by explaining high-temperature properties of turbine wheels heat treated by normalizing and tempering, oil quenching and tempering, and an interrupted quench and temper. Data are presented in this report for a limited number of tests to survey the stress-rupture, total deformation, and creep rate properties of six isothermally transformed structures, as well as normalized and tempered and oil quenched and tempered structures of bar stock material in the temperature range of 700' to 1200'F. Whenever transformation characteristics permitted, three structures transformed in the pearlitic transformation range and three in the bainitic range have been studied. Four steels were used with varying degrees of transformation characteristics. Principles of Heat Treatment When the hardness level is restricted to approximately 300 BHN, transformation conditions must be controlled to produce either bainite or martensite. Vanadium bearing steels apparently are not quite so restricted in that transformation in the lower part of the pearlitic region also will meet this requirement. Within these restrictions, the principles of heat treatment for service at high temperatures may be summarized as follows: 1. Conditions of heat treatment producing bainite will give, on an average, maximum or near maximum strengths over the temperature range of 700' to 12000F for criteria of strength based on times between 100 and 1000 hours. 2. Within the generalization that bainite is the preferred structure for strength there is considerable variation. 20

For 4340 steel, maximum strength progresses from lower to middle to upper bainite with increasing temperature. In each case there is generally a substantial margin in favor of one of the bainites and a considerable penalty for one of the others. Thus, there is an incentive for precise control of structure versus service temperature. For "I17-22A"S steel, the bainitic structure having the maximum strength varied less regularly with test temperature and criterior of strength. What is perhaps more important is that one of the bainites, at almost all temperatures, tended to be well on the low side of the strength range. Again, there is considerable value in precise structure control, at least to avoid the low strength bainitic structures, and at 7000 to 9000F to obtain the maximum strength. 3. Normalizing of the bar stock generally produced near maximum strengths for both steels. Apparently a range in bainitic structures, together with some martensite produces a good average structure. In those cases where the normalized structure compared unfavorably with one or more of the "pure" structures, it will be noted that it had strengths near to those of the pure structures it most closely resembled. For normalizing to produce a high level of properties, the cooling rate should be such as to allow the major part of the transformation to occur in the bainitic region. A predominance of martensite or pearlite due to section size and transformation characteristics could have inferior properties. 4. The survey creep, total deformation, and rupture data show that martensitic structures tend to fall off in comparative strength to the other structures with increasing temperatures and time for a given criterion of strength. The differences are quite substantial in comparison to the strongest bainitic structure, with the possible exception of "17-22A'"S steel at 11000F. It should also be noted that at most of the temperatures the martensite outranks at least one of the bainitic structures. Only in the case of "17-22A"S at 700F did the martensitic structure give better properties than the normalized bar stock. There is some indication that martensitic structures tend to undergo less deformation during first-stage creep, but have higher secondary creep rates so that they can compare more favorably on the basis of limited deformations at short-time periods. 5. The limited rupture data did not show a predominant variation in elongation and reduction of area in rupture tests for the bainitic structures, martensite or normalized stock for 4340 steel. The same is largely true for "1722A"S steel except that slightly lower values seem characteristic of lower bainitic and the normalized structures at 1100~F and for middle bainite and the normalized structures at 1200~F. The data for H-40 show that although all 21

structures gave exceptionally good elongation and reduction of area values at 700~, 900~, and 1200~F, the normalized structure exhibited extremely low ductility at 1100~F. The other structures gave good ductility at 1100F, although the bainitic material tended to show slightly lower values than the pearlitic and martensitic bar stock. Where lower hardness values than 300 BHN are permissible, consideration can be given to pearlitic structures. The following principles appear to govern the use of pearlitic structures: 1. Pearlitic structures have low comparative strengths at low temperatures due to low tensile and yield strengths. In the case of t"17-22A"S steel, where lower and middle pearlite may have relatively high hardness, their strengths were only slightly below the bainitic structures. Thus, pearlitic structures would not ordinarily be suitable for use at 700~ and 900~F except for relatively low stress applications. Fine to medium pearlite in "17-22A"S steel would not, however, be particularly harmful provided secondary hardening kept the hardness up. 2. Because pearlites compare far more favorably at the higher temperatures, little or no sacrifice in strength may be involved by using pearlitic structures. It should be noted, however, that lower (fine) pearlite appeared to be unduly weak in both 4340 and "17-22A"S steels at the higher temperature. If pearlitic structures are to be used at the higher temperatures, relatively coarse pearlite from transformation in the upper part of the pearlite range should be obtained. 3. The presence of some pearlite in a steel of the type of "17-2ZA"S apparently would not be particularly detrimental at any temperature provided the hardness was sufficiently high. 4. Although data are sparse, there was no indication that pearlitic structures had any significantly better elongation and reduction of area in rupture tests at any temperature. In fact, the upper pearlite with high strength at the higher temperatures tended to have the lowest values. Relationship between Type of Structure and Chemical Composition The data are reported and discussed in terms of the types of microstructure without regard to alloy content. It should be recognized, however, 22

that the alloy content influences the level of strength for the various structures. This was true even at 700F where the 4340 had lower strength than the "17-22A'S even at the same initial hardness. Apparently "17-22A"S also was superior to H-40 for similar structures at 700~F. The "17-22A"S structures maintained strength better with increasing temperature than the 4340 steel. It was necessary to go to higher temperatures and longer time periods before the influence of increased alloy content became more apparent. Thus, at 1000 hours at 1100~F, the H-40 material was stronger than "17-22A"S and the C-422 was stronger than the H-40 for similar bainitic and martensitic structures. Since the H-40 and C-422 steels could not be transformed to a true pearlitic structure, comparisons of this type of structure are difficult to make. However, the "pearlitic" H-40 structure, which was actually more nearly a spheroidized structure, was considerably stronger at 1200~F than the "17-22A"S pearlitic structures for 100-hour rupture times. Estimation of Strengths from Microstructures The correlation of microstructures for continuously cooled normalized bar stock and for the turbine wheels indicates that reasonably good estimates of probable strength can be made from microstructure. In the case of the wheels, this was aided by not too much variation in strength between the structures involved. It is doubtful that microexamination alone would be good enough to determine whether the structure with the very highest strength had been obtained or not. The wheels had generally higher short time strengths than the isothermally transformed structures. There was also a slight tendency for the normalized bar stock to do likewise. It is uncertain whether or not this was due to continuous cooling transformation or to other factors not yet established. Certainly this could not have been predicted from present knowledge of microstructure s. The variation between heats of "17-22AtS steel with similar microstructure in the pearlitic range was not evident from the microstructure. If the variation was due to secondary hardening or to minor differences in transformation characteristics, it is doubtful if microstructures would ever be useful for establishing such variations. At present, microstructure examination showing predominantly bainitic structures indicate a relatively high level of strength. It is possible that some estimate could be made of the relative level within the range for bainites, although 23

this is difficult for steels of the "17-22A"S type. The relative strengths from martensitic or pearlitic structures could also be estimated. The variation within the types of pearlite probably could also be estimated. Limitations of Results Experience indicates that the relations developed between structure and properties are quite reliable for the steels when heat treated at the usual temperatures. In using the results of this investigation, however, due consideration should be given to a number of factors: 1. The survey of properties was very limited. Careful analysis of the data suggests that a few of the values ought to be checked before too much reliance on detail of results is accepted. 2. The relative strengths for various time-temperature-total deformation-creep conditions could be fairly complex for the structures. This has not been well covered by the survey tests. Thus, more complete testing of structures might well show the relationships for varying service requirements better than the data reported. In particular, caution should be used where comparisons were based on time for fracture, time for a limited total deformation, or on creep rates at single stresses. Such comparisons often suggest much wider differences than the more practical evaluation of the variation in stress for fracture or total deformation in a given time period or the stress for a given creep rate. 3. One of the most severe limitations is the omission of checks between heats or determination of the effect of varying prior history. The two heats of "17-22A"S bar stock suggest that at least in the pearlite region substantial variations can be present even when the transformation diagrams indicate no great difference. 4. Only one temperature of heat treatment was involved for each steel. The influence of varying this factor on relative strengths of the structures was not checked. Likewise, any effects of tempering conditions have not been studied or the effects of tempering to varying hardness levels. 5. The evaluation of relative strengths for continuously cooled structures has not been well checked. The evaluation seems quite good on a qualitative basis for normalized bar stock and for forged wheels. However, the 24

higher strengths at short time periods suggest that estimations of strength of continuously cooled structures, other than martensite, should be checked further. CONCLUSIONS A survey of the variations in properties at 700' to 12000F of four low alloyed hardenable steels with possible variations in microstructure has been carried out. The survey covered martensitic, bainitic, and pearlitic structures obtained by isothermal transformation. Tempering was used to reduce hardness to 300 Brinell when the structure was initially harder. Principles developed were checked against the properties of normalized bar stock and heat-treated turbine wheels. The results indicate the following conclusions: 1. Wide ranges in structure were easily obtainable in SAE 4340 and a 1. 25 Cr - 0. 75 Si - 0. 5 Mo - 0. 25 V steel. Increased sluggishness of transformation limits the range of structures possible in reasonable time periods for the 3 Cr - 0.5 Mo - 0. 5 W - 0. 8 V steel, while the structure of a 13 Cr - 1 Mo - 0. 8 W - 0. 25 V steel was limited to tempered martensite at 300 Brinell hardness. 2. In those steels subject to transformation within the pearlitic and bainitic regions in reasonable time periods, a substantial range in properties is possible. In general, bainitic structures had the maximum strength over the entire temperature range. Martensite ranged from medium to low strength with increasing temperature. Pearlites increased in relative strength with increasing temperature to approximately the same level as the bainites at the highest temperature s. 3. Within each type of structure, considerable variation in strength can exist. In general, the maximum strength shifted from structures produced by transformation in the lower part of the bainite or pearlite regions of the transformation diagram to the upper temperature regions as the test temperature increased. There were variations in this, particularly for vanadiumbearing steel where secondary hardening characteristics probably influence the strength of the individual structures. In addition, there were shifts in relative strength, depending on the criterion of strength used at individual temperatures. 25

4. In most cases, surprisingly wide ranges in structure had similar strengths at elevated temperatures. In almost every case, there were, however, outstandingly strong or weak structures. 5. Normalizing generally results in a high level of strength because it tends to produce predominantly bainitic structures. It should be recognized, however, that in normalizing the section size and transformation characteristics of the steel must be such as to cause bainites to form for this generalization to hold. 6. Reasonably good correlation between structures and properties of turbine wheels was obtained by applying the results of this investigation. Some discrepancy was observed in that the wheels had higher strengths at short time periods than were observed for the isothermal structures. 7. The generalities stated for the relations between structure and properties apparently hold quite well for the steels investigated. The structures, however, do not indicate level of properties for different steels. Alloy content influences the actual strengths. The low Cr - Mo - V steel was superior to 4340 at all temperatures. The higher alloyed steels only became superior to the low Cr - Mo - V steel at the higher temperatures and longer time periods. 8. The trends shown by the data appear to be quite reliable. However, the test data were limited in many respects and due consideration should be given to the limitations. BIBLIOGRAPHY 1. A. Zonder, A. I. Rush, J. W. Freeman, "High-Temperature Properties of Four Low-Alloy Steels for Jet-Engine Turbine Wheels". Wright Air Development Center Technical Report 53-277, Part I (November, 1953). 2. United States Steel Corporation, "Atlas of Isothermal Diagrams" (1951). 26

TABLE I TYPE STRUCTURES, HEAT TREATMENTS AND ACTUAL STRUCTURES FOR 4340 STEEL (All 4340 bar stock austenitized at 1750~F for 1 hour.) Transformation Approximate Structure Tempering Aim Structure Conditions Obtained B H N B H N ___________ Temp('F) Time (hrs) ___Temp (*F) Time(hrs) Upper Pearlite 1240 10 80% medium pearlite + 212/221 None -- 12/221 20% ferrite Middle Pearlite 1150 14 95% fine pearlite and fine 197/233 None _ 197/233 carbide-ferrite aggre-a gate + 5% ferrite Lower Pearlite 1050 111 99% very fine carbide- 255/275 None - 255/275 ferrite aggregate + 1% ferrite Upper Bainite 850 28 70%coarsebainite + 30% 319/327 None 319/327 martensite Middle Bainite 750 24 100% medium acicular 293/313 None 293/313 bainite Lower Bainite 650 1-1/2 100% fine acicular bainite 430 1100 1-1/4 277/301 Normalized Air Cooled from 1750 35% martensite + 65% 385 1100 1 300/311 bainites Oil Quenched Oil Quenched from 100% martensite 585 1100 10 304/309 1750

TABLE II TYPE STRUCTURES, HEAT TREATMENTS AND ACTUAL STRUCTURES OF 1.25 Cr-Mo-Si-V ("17-22A"S) STEEL (All "17-22A"S bar stock austenitized at 1750'F for 1 hour.) Transformation Approximate Structure Tempering Aim Structure Conditions Obtained B H N B H N T__________ emp (F) Tiie (hrs) ________ -Temp (F) Time (hrs) Upper Pearlite 1300 1-1/2 45% medium pearlite + 196/237(a) None -- 196/237 55% ferrite Middle Pearlite 1225 1-1/2 40% medium fine pearl- 266/285 None - 266/285 ite + 60% ferrite Go Lower Pearlite 1150 10 40% fine pearlite + 60% 375 1200 12 263/313 ferrite Upper Bainite 900 2 60% redum bainite + 465 1200 16 284/327 40% martensite Middle Bainite 800 1/2 97% fine acicular bain- 360 1200 4 307/310 ite + 3% martensite Lower Bainite 700 1/12 100%fine acicular bainite 365 1200 12 273/302 Normalized Air Cooled from 1750 15% martensite + 85% 355 1200 10 302/313 coarse bainites Oil Quenched Oil Quenched from 100% martensite 525 1300 1 272/310 1750 (a) Hardness values of approximately 310 were obtainedfor this transformation temperature for Heat No. 24797. Hardnesses reported are for Heat 10420.

TABLE III TYPE STRUCTURES, HEAT TREATMENTS AND ACTUAL STRUCTURES FOR 3 Cr-Mo-W-V (H-40) STEEL (All H-40 bar stock austenitized at 1950 F for 1 hour.) Transformation Approximate Structure Tempering Aim Structure Conditions Obtained B H N ________ B H N N ____________ Temp (F) Time (hrs ______ _ _____ Temp (F) Time (hrs) _____ Pearlite 1300 24 fine carbide precipitate 190/200 None 190/200 Bainite 750 10 100% bainite 480 1300 1 293/313 Normalized Air Cooled from 1950 20% martensite + 80% 435 1200 18 310/321 bainite s Oil Quenched Oil Quenched from 100% martensite 523 1200 12 290/323 1950

TABLE IV RUPTURE, TOTAL DEFORMATION, AND CREEP DATA AT 700', 900-, 1000~, AND 1100F FOR ISOTHERMALLY TRANSFORMED 4340 STEEL Stress Rupture Elongation Reduction Deformation Time to Reach Specified Minimum Structure BHN Time of Area on Loading Total Deformation (hours) Creep Rate ___(psi) (hours) (% in 1 in.) (%) (in. /in. ) 0. 1T 0.2%..5 1. 0O (%/hour) 700~F Middle Pearlite 199 90,000 10.7 23.0 57.0 0.03274 a a a a -- Lower Pearlite 221 90,000 98.8 21.8 56.5 0.01650 a a a a 0.0432 Upper Bainite 324 90,000 1316 (d) -- -- 0.00465 a a 1 198 0.00032 Middle Bainite 309 90,000 1315 (d) -- -- 0.00472 a a " 1 1291 0.00019 Lower Bainite 277 90,000 1485 (d) -- -- 0.00440 a a,1 2000(b) 0.00016 Oil Quenched 304 90,000 1350 (d) -- -- 0.00430 a a 2 675 0.00027 Normalized 300 90,000 1294 (d) - -- 0.00467 a a 1 1000 0.00016 900'F Upper Pearlite 217 55,000 4.5 51.0 68.8 0.01502 a a a a -- 219 40,000 108.6 23.0 35.0 0.00475 a a -- -- Middle Pearlite 231 55,000 9.7 28.0 56.0 0.00701 a a a <1 -- 295 40,000 326.2 10.0 11.0 0.00225 a a 4 35 0.0125 Lower Pearlite 260 55,000 20 34.5 37.9 0.00313 a a <1'v1 0.55 255 40,000 402.3 5.0 5.0 0.00177 a <1 19 125 0.00387 Upper Bainite 325 55,000 1215 6.0 6.4 0.00265 a a 6 48 0.00163 320 40,000 1105 (d) -- -- 0.00268 a a 8 125 0.00019 Middle Bainite 313 55,000 1417 4.1 (c) 4.7 0.00380 a a 1 51 0.00064 302 40,000 1009 (d) -- -- 0.00260 a a 60 2200(b) 0.00021 Lower Bainite 277 55,000 897 18.5 (c) 15.4 0.00250 a a 8 51 0.0053 290 40,000 1985(d) -- -- 0.00243 a a 38 225 0.00107 Oil Quenched 306 55,000 381 19.5 39.5 0.00269 a a 2 13 0.0148 302 40,000 2338 4.0 5.5 0.00175 a <1 50 355 0.00111 Normalized 300 55,000 842 12.0 22.4 0.00260 a a 8 64 0.00414 300 40,000 1919 (d) -- -- 0.00164 a 5 1160 >3000(b) 0.00015 30

TABLE IV, Continued Stress Rupture Elongation Reduction Deformation Time to Reach Specified Minimum Structure BHN Time of Area on Loading Total Deformation (hours) Creep Rate (psi) (hours) (% in 2 in.n.(%) (in. 1 0.. 5, 1.0% (%/hour) 1000~F Upper Pearlite 219 13,000 1103 (d) -- -- 0.00044 6 63 528 1400(b) 0.00057 Middle Pearlite 225 31,000 52.2 10.0 9.5 0.00169 a -- -- -- -- 197 15,000 989 (d) -- -- 0.00116 a 10 135 570 0.00113 229 13,000 1539 (d) -- - 0.00053 10 52 515 1175 0.00060 Lower Pearlite 270 13,000 848 21.4 24.8 0.00068, 2 6 46 141 0.00537 Upper Bainite 327 31,000 389 10.0 10.1 0.00185 a <1 10 75 0.0072 325 20,000 1736 5.2 5.6 0.00118 a 10 130 475 0.00124 325 15,500 1005 (d) -- -- 0.00096 <1 25 470 1500(b) 0.00042 322 13,000 1075 (d) -- -- 0.00057 5 91 1130(b) -- 0.00023 Middle Bainite 295 31,000 261 5.9 5.6 0.00190 a <1 18 85 0.0070 291 20,000 1518 3.0 4.1 0.00119 a 4 85 450 0.00145 307 13,000 1706 (d) -- -- 0.00068 4 42 472 1920(b) 0.00030 Lower Bainite 291 31,000 210 9.4 17.0 0.00161 a <1 6 26 0.0179 294 13,000 1035 (d) -- -- 0.00055 2 32 300 1104(b) 0.00053 Oil Quenched 310 30,000 182 10.9 14.1 0.00144 a 1 4 20 0.022 309 19,000 918 12.6 15.0 0.00094 <1 8 70 245 0.00295 306 13,000 1025 (d) -- -- 0.00060 3 27 248 628 0.00115 Normalized 290 31,000 371 5.5 7.4 0.00126 a 5 50 145 0.00505 300 20,000 1392 5.0 4.0 0.0009 ^'1 20 228 650 0.00116 301 12,000 1000 (d) -- -- 0.00050 12 114 802 2150(b) 0. 00037 1100"F Upper Pearlite 218 18,000 21.7 28.0 27.0 0.00152 a -- -- 212 4,500 1146 (d) -- -- 0.00053 52 235 893 1900(b) 0.00046 Middle Pearlite 217 18,000 43.5 7.5 8.6 0.00097 -- -- -- -- -- 233 4,500 1148 (d) -- -- 0.00024 25 93 315 643 0.00139 Lower Pearlite 255 18,000 27.2 7.0 11.4 0.00108 a -- -- "4.5 -- 275 4,250 1007 (d) -- -- 0.00032 9 21 90 217 0. 00390 Upper Bainite 323 18,000 106 12.2 11.6 0.00130 -- -- -- -- -- 319 4,500 990 (d) -- -- 0.00026 17 78 552 1600 (b) 0.00048 Middle Bainite 293 18,000 80 8.2 10.2 0.00080 -- -- -- 18 -- 302 4,500 1343 (d) -- -- 0.00025 13 55 432 1550(b) 0. 00044 Lower Bainite 293 18,000 54.2 12.6 16.8 0.00139 a -- -- 7 -- 301 4,500 1008 (d) -- -- 0.00042 3 19 156 436 0.00172 Oil Quenched 290 18,000 43.5 20.0 25.2 0.00148 a -- -- -- 309 4,500 1080 (d) -- -- 0.00027 5 22 104 258 0.0024 Normalized 293 18,000 69.6 7.0 11.7 0.00116 a -- -- -- -- 299 6,000 1150(d) -- -- 0.00035 8 26 100 286 0.0026 311 4,000 1056 (d) -- -- 0.00017 18 96 484 1400(b) 0.00052 292 2,000 1060 (d) -- -- 0.0001 86 302 1550(b) -- 0. 00022 (a) Specimen reached this deformation in loading. (b) Extrapolated value. (c) 0. 250-inch diameter specimen, elongation percent in one inch. (d) Test discontinued at this time. 31

TABLE V RUPTURE, TOTAL DEFORMATION, AND CREEP DATA AT 700~, 900-, 1100, AND 1200FZ FOR ISOTHERMALLY TRANSFORMED STRUCTURES OF A 1.25 CR-MO-SI-V ("17-22A"S) STEEL Stress Rupture Elongation Reduction Deformation Time to Reach Specified Minimum Structure BHN Time of Area on Loading Tta Deformation (hours) Creep Rate __(psi) (hours) (% in 2 in.) (%) (in. /in.) 0. 1h 0. Z 0. 5% 1. (%/hour) 700*F Upper Pearlite 233(g) 69,000 1080 (d) -- -- 0.0024 a a (h) (h) 0.00003 Middle Pearlite 267 115,000 265.2 20.0 (c) 59.2 0.0095 a a a <1 0.0095 295 95,000 1105 (d) -- -- 0.00495 a a -- >2000(b) 0.00008 Lower Pearlite 263 115,000 (f) 19.0 (c) 61.0 - -- -- 290(g) 93,000 1080 (d) -- -- 0.0176 a a a a 0.00019 Upper Bainite 284 115,000 147 20.2 (c) 62.0 0.0071 a a a <1 0.0180 (g)108,000 1105 (d) -- -- 0.0056 a a a 1000 0.0001 Middle Bainite 309 115,000 1827(d) -- -- 0.0061 a a a 45 0.00029 309 104,000 1105 (d) -- -- 0.0051 a a a >2000(b) 0.00005 Lower Bainite 275 115,000 59.4 18.8 (c) 66.7 0.00815 a a a <1 0.0452 Oil Quenched 278 115,000 289 19.8 (c) 63.3 0.0067 a a a 1 0.0095 298(g)107,000 1145 (d) -- -- 0.0055 a a a 1000 0.0001 Normalized 302 115,000 132 21.0 (c) 61.9 0.0066 a a a 1 0.0220 307 102,000 1145(d) -- -- 0.00465 a a e 1 >2000(b) 0. 00007 900'F Upper Pearlite 196(g) 70,000 112 29.0 (c) 60.0 0.01479 a a a a 0.0576 Middle Pearlite 266 70,000 1484 13.0 (c) 25.0 0.00570 a a a 24 0.0023 Lower Pearlite 266 70,000 1205 (d) -- -- 0.00406 a a 2 53 0.00223 Upper Bainite 289 70,000 686 30.0 (c) 59.5 0.00355 a a 1 50 0.00504 Middle Bainite 307 70,000 1648 (d) -- -- 0.00323 a a 65 2500(b) 0.00014 Lower Bainite 283 70,000 1456 24.0 (c) 56.2 0.00350 a a 12 362 0.00115 Oil Quenched 272 70,000 756 30. 3 (c) 64.0 0.00378 a a 3 50 0.00384 Normalized 303 70,000 1482 (d) -- -- 0.00335 a a 24 1400 0.00030 32

TABLE V, Continued Stress Rupture Elongation Reduction Deformation Time to Reach Specified Minimum Structure BHN Time of Area on Loading Total Deformation (hours Creep Rate (psi) (hours) (% in 2 in.) (%) (in. /in.) 0.1% 0. Z. % 5% 1.0% (%/hour) 1100'F Upper Pearlite 196(g) 41,000 4.4 22.2 27.0 0.00510 a a a -- -- 238(g) 19,000 1298 (d) -- -- 0.0009 3 75 475 958 0.00072 309 19,000 565 4.4 5.1 0.00082 1 17 159 336 0.00204 313 15,000 1095 (d) -- -- 0.0006 14 108 622 1460(b) 0.00059 Middle Pearlite 285 19,000 669 (e) 3.0 2.8 0.00110 a 10 185 430 0.00145 Lower Pearlite 290(g) 41,000 42.0 8.5 8.7 0.00226 a a 4 12 -- 291 15,000 652 15.5 17.1 0.00065 24 54 107 218 0.00340 Upper Bainite 310(g) 41,000 51.5 7.2 8.6 0.00269 a a 4 13 -- 327 19,000 796 5.8 6.6 0.00110 a 8 177 447 0.00140 317 15,500 1007(d) -- -- 0.00073 5 65 388 798 0.00094 Middle Bainite 309 41,000 88.2 5.1 4.9 0.00217 a a 6 19 -- 310 19,000 815 4.0 (c) 3.0 0.00096 a 30 222 575 0.0015 Lower Bainite 290 (g) 41,000 92.8 5.0 4.0 0.00252 a a 9 32 0.0165 -- 21,000 889 2.0 5.6 0.00174 a 6 198 604 0.00113 303 14,000 1033 (d) -- -- 0.00078 2 67 621 1700(b) 0.00043 Oil Quenched 293 41,000 23.4 28.0 27.5 0.00173 a a a a 0.0065 306 20,000 666 4.5 -- 0.0011 1 13 139 345 0.00186 302 15,000 1061 (d) -- -- 0.00079 <1 50 470 1006 0.00085 Normalized 309 41,000 111.5 2.5 3.1 0.00212 a a 26 -- 0.00614 311 20,000 773 2.0 -- 0.00090 1 46 375 656 0.00086 317 17,000 1035(d) -- -- 0.00079 14 177 875 1200(b) 0.00045 291 14,000 1150 (d) -- -- 0.00065 50 230 1200 -- 0.0003 302 10,000 1060(d) -- -- 0.0004 32 140 1700(b) -- 0.00016 1200'F Upper Pearlite 219(g) 14,000 215.1 6.5 8.8 0.00056 3 12 47 103 0. 0072 237(g) 7,500 1892 2.0 (e) 0.00030 40 182 590 1050 0.00066 Middle Pearlite 302 14,000 132.4 6.0 7.1 0.00056 2 7 23 51 0.0162 276 7,500 1033 10.0 (e) 0.00034 10 46 196 370 0.00198 Lower Pearlite 293(g) 14,000 100.2 10.2 10.4 0.00093 <1 4 15 31 0.028 293 7,500 349 17.0 (e) 0.00040 8 20 67 120 0.00656 Upper Bainite 310(g) 14,000 84.7 7.4 9.4 0.00086 <1 5 17 -- - 320 7,500 456 22.5 (c) 35.8 0.00054 1 8 45 104 0.00810 Middle Bainite 309 14,000 151.6 6.2 7.9 0.00098 a 9 41 87 0.00845 310 7,500 812 19.1 (c) (e) 0.00050 10 26 115 228 0.00316 Lower Bainite 299(g) 14,000 104.4 7.0 13.2 0.00112 a 5 20 45 0.019 273 7,500 709 22.9(c) 34,6 0.00048 6 30 112 229 0.00360 Oil Quenched 298 14,000 73.1 8.0 14.9 0.00096 a 4 14 -- 310 7,500 575 30.0 39.8 0.00058 6 17 69 144 0.00660 Normalized 304 14,000 167.1 4.0 5.0 0.00066 5 20 65 140 0.00640 313 7,500 918 10.0 14.9 0.00046 6 46 176 333 0.00230 (a) Specimen reach this deformation on loading. (b) Extrapolated value. (c) 0. 250-inch diameter specimen, elongation percent in one inch. (d) Test discontinued at this time. (e) Broke in shoulder radius. ( f) Broke on loading. (g) Heat No. 10420; all other tests Heat No. 24797. (h) Deformation not obtained during testing period and would have required excessive extrapolation. 33

TABLE VI RUPTURE, TOTAL DEFORMATION, AND CREEP DATA AT 700', 900', 1100', AND 1200'F FOR ISOTHERMALLY TRANSFORMED H-40 STEEL Stress Rupture Elongation Reduction Deformation Time to Reach Specified Minimum Structure BHN Time of Area on Loading Total Deformation (hours) Creep Rate (psi) (hours) (% in 2 in.) (%) (in. /in) 0. 1 0.1 Z1' 0. 50. 1.0 0% (%/hour) 700~F Pearlite 193 90,000 24 22.0 (c) 61.0 0.03306 a a a a Bainite 293 90,000 1170 (d) -- -- 0.00324 a a 1040 (g) 0.00010 Oil Quenched 290 90,000 1514 (d) -- -- 0.00410 a a 15 2000(b) 0.00019 Normalized 310 90,000 1292 (d) -- -- 0.00416 a a 13 1700(b) 0.00017 900~F Pearlite 198 65,000 3.3 22.0 (c) 68.0 0.01080 a a a a -- Bainite 309 65,000 1193 (d) -- -- 0.00332 a a 21 297 0.00027 Oii Quenched 290 65,000 917 31.0 (c) 68.0 0.00359 a a 1 50 0.00463 Normalized 320 65,000 1052 18.0 (c) 36.0 0.00301 a a 10 85 0.00328 1100'F Pearlite 190 30,000 23 49.0 82.0 -- -- -- Bainite 313 35,000 405 12.0 (c) 33.0 0.00140 a <1 13 110 0.00585 295 31,000 930 10.3 20.0 0.00021 a a 52 232 0.00239 308 28,000 1005(d) -- -- 0.00168 a a 132 470 0.00144 312 23,000 1095(d) -- -- 0.00101 a 36 396 843 0.00073 Oil Quenched 320 40,000 136 12.5 46 0.00232 a a 10 39 0.016 321 30,000 865 20.0 26.0 0.00150 a 2 94 279 0.00237 323 24,000 1032(d) -- -- 0.00120 a 24 300 862 0.00083 Normalized 315 43,000 48.4 (f) -- 0.00226 a a 27 -- 0. 0058 310 40,000 193 5.0 13.6 0.00231 a a 20 89 0.0074 312 34,000 272 (e) -- 0.00165 a 6 162 -- 0.00148 320 31,000 720 (e) -- 0.00152 a 7 274 677 0.00105 316 27,500 1130 (d) -- -- 0.00135 a 36 430 1054 0.00064 1200~F Pearlite 200 25,000 142 23.0 58.0 0.00198 a a 13 47 Bainite 293 25,000 86 27 (c) 52 0.00177 a -- 4 18 Oil Quenched 300 25,000 62 45 74 0.00185 a <1 4 14 Normalized 315 25,000 100 17 45 0.00142 a 1 9 38 (a) Specimen reached this deformation on loading. (b) Extrapolated value. (c) 0. 250-inch diameter specimen, elongation given as percent in one inch. (d) Test discontinued at this time. (e) Specimen fractured in shoulder radius. ( f) Specimen fractured in threaded end. (g) Would have required excessive extrapolation for duration of test. 34

TABLE VII RUPTURE, TOTAL DEFORMATION, AND CREEP DATA AT 1100F FOR HEAT TREATED BAR STOCK OF C-422 STEEL Stress Rupture Elongation Reduction Deformation Time to Reach Specified Total Deformation Minimum Treatment BHN Time of Area on Loading (hours) Creep Rate ~______ _ (psi) (hours) (% in 2 in.) (%i) (in. /in.. ) 0. 510 5 1. 0%7 (%/hour) (JI 1100'F OilQuenched 307 30,000 1003 (d) -- - 0.00159 a'1 133 951 0.00049 Normalized 306 39,000 366 20.9 69.1 0.00214 a a 9 46 0.00628 Normalized 299 35,000 816 19.6 46.5 0.00204 a a 16 157 0.00224 Normalized 303 30,000 1120 (d) -- - 0.00153 a u3 112 690 0.00088

TABLE VIII RUPTURE, TOTAL DEFORMATION, AND CREEP STRENGTHS AT 1000~ AND 1100F FOR TURBINE WHEELS AND ISOTHERMALLY TRANSFORMED BAR STOCK OF SAE 4340 STEEL Rupture Strength One-Percent 0. 001%o /Hour Structure (psi) Total Deformation Creep Strength Strength (psi) 100-hr 1000-hr 100-hr 1000-hr (psi) 1000"F Upper Pearlite -- -- -- 14,000 (15,000) Middle Pearlite 26,000 (16,000) -- 13,000 14,500 Lower Pearlite -- 12,000 14,000 Upper Bainite 46,000 23,000 29,000 17,000 19,000 Middle Bainite 39,000 22,000 29,000 16,000 18,000 Lower Bainite 38,000 (20,000) 24,000 13,000 15,000 Oil Quench. Barstock 35,000 18,500 23,000 11,000 12,000 Norm. Barstock 46,000 22,000 33,000 17,000 19,000 Norm. Disk 48,000 24, 000 43,000 17,000 25,000 Oil Quench. Disk 38,000 15,000 23,000 Int. Quench Disk 48,000 22,000 46,000 17,000 1100*F Upper Pearlite (12,000) - - 6,000 Middle Pearlite (15,000) -- 3,000 Lower Pearlite (13,000) -- 7,000 Upper Bainite 18,000 -- -- 6,000 Middle Bainite 17,000 -- 13,000 6,000 Lower Bainite 15,000 -- 11,000 2,000 Norm. Barstock 16,500 -- 8,000 4,500 -- OilQuench. Barstock (14,000) -- 9,000 - Norm. Disk 18,000 -- 11,000 Oil Quench. Disk 16,000 -- (6,000) Int. Quench Disk 19,000 -- 15,000 ( ) Indicate approximate values. 36

TABLE IX RELATIVE STRENGTHS OF STRUCTURES FOR 4340 STEEL Temp Order f Strength of Microstructures Criterion of Strength Normalized ('F) First Second Third Fourth Fifth Sixth Seventh Bar Stock 700 Hours for 1.0% lower middle marten- upper lower middle total deformation bainite bainite site bainite pearlite pearlite at 90,000 psi 2020 (a) 1291 675 198 (b) (b) 1000 Minimum creep lower middle marten- upper lower miille rate at 90, 000 psi bainite bainite site bainite pearlite pearlite (%/hr) 0.00016 0.00019 0.00027 0.00032 0.0432 (c) 0.00016 900 Hours for 1. 0% middle marten- lower upper lower middle upper total deformation bainite site bainite bainite pearlite pearlite pearlite at 40,000 psi 2200 (a) 355 225 125 125 35 (c) >3000(a) Minimum creep upper middle lower marten- lower middle upper rate at 40,000 psi bainite bainite bainite site pearlite pearlite pearlite (%/hr) 0.00019 0.00021 0.00107 0.00111 0.00387 0.0125 (c) 0.00015 Hours for rupture middle upper lower marten- lower middle upper at 55,000 psi bainite bainite bainite site pearlite pearlite pearlite 1417 1215 897 381 20 9.7 4.5 842 1000 Stress for 1.0% upper middle upper lower middle marten- lower total deformation bainite bainite pearlite bainite pearlite site pearlite in 1000 hours (psi) 17,000 16,000 14,000 13,000 13,000 11,000 (c) 17,000 Stress for rupture upper middle upper lower marten- middle lower in 1000 hours (psi) bainite bainite pearlite bainite site pearlite pearlite 23,000 22,000 (a) 20,000(a) 18,500 16,000(a) 12,000 22,000 1100 Stress for rupture upper middle lower middle marten- lower upper in 100 hours (psi) bainite bainite bainite pearlite site pearlite pearlite 18,000 17,000 15,000 15,000(a) 14,000(a) 13,000(a) 12,000(a) 16,500 (a) Estimated values. (b) Exceeded value on loading. (c) Not determined due to low strength. Note: 100% indicated structures except for upperbainite which contained 30% martensite. Normalized structure - 65% bainites + 35% martensite. 37

TABLE X RUPTURE, TOTAL DEFORMATION, AND CREEP STRENGTHS AT 1100~ AND 1200~F FOR TURBINE WHEELS AND ISOTHERMALLY TRANSFORMED BAR STOCK OF "17-22A"S STEEL Rupture Strength One-Percent 0. 001%/Hour Structure (psi) Total Deformation Creep Strength Strength (psi) 100-hr 1000-hr 100-hr I000-hr (psi) 1 100~F Upper Pearlite (25,000) (17,500)a (22,000) 16,000 16,500 Middle Pearlite -- 17,500 --- 17,000 Lower Pearlite 30,000 13,000 22,000 -- (10,000) Upper Bainite 34,000 18,000 28,000 14,000 16,000 Middle Bainite 39,000 18,000 30,000 15,000 15,000 Lower Bainite 40,000 20,000 33,000 17,000 20,000 OilQuench. Barstock 30,000 18,000 26,000 15,000 15,000 Norm. Barstock 44,000 18,000 (34,000) 18,000 22,000 Oil Quench. Disk 41,000 19,000 36,000 17,000 21,500 Int. Quench Disk 42,000 22,000 Norm. Disk 35,000 15,500 - 1200'F Upper Pearlite 17,000 9,000 14,000 7,500 Middle Pearlite 15,000 7,600 12,000 4,000 Lower Pearlite 14, 000 (4,400) 8,000 Upper Bainite 13,000 5,600 7,500 Middle Bainite 16,500 7,000 13,000 Lower Bainite 14,500 6,700 11,000 (2,000) Oil Quench. Barstock 12,500 6,400 9,000 - Norm. Barstock 17,000 7,200 16,000 (3,000) Oil Quench. Disk 14,000 -- 11,000 Int. Quench Disk - - - Norm. Disk - - - - -- (a) Based on Heat 10420 which gave low hardness. ( ) Indicate approximate values. 38

TABLE XI RELATIVE STRENGTHS OF STRUCTURES FOR "17-22A"S STEEL Temp Order of Strength of Microstructures Criterion of Strength Normalized ('F) First Second Third Fourth Fifth Sixth Seventh Bar Stock 700 Stress for creep rate middle upper marten- middle lower lower upper of 0. 0001%/hr (psi) bainite bainite site pearlite pearlite bainite pearlite 108,000 108,000 107,000 96,000 93,000, 91,000 72,000 103,000 Hours for rupture at middle marten- middle upper lower lower upper 115,000 psi bainite site pearlite bainite bainite pearlite pearlite >1827 289 265.2 147 59.4 broke on (a) 132 loading 900 Hours for 1. 0% total middle lower lower marten- upper middle upper deformation at bainite bainite pearlite site bainite pearlite pearlite 70,000 psi 2500(b) 362 53 50 50 24 (c) 1400 Hoirs for rupture at middle middle lower lower marten- upper upper 70,000 psi bainite pearlite bainite pearlite site bainite pearlite >1648 1484 1456 >1205 756 686 112 >1482 1100 Stress for 1. 0% total lower upper middle middle marten- upper lower deformation in 1000 bainite pearlite pearlite bainite site baiiite pearlite hours (psi) 17,000 16,000 16,000(d) 15,000 15,000 14,000 (a) 18,000 Stress for creep rate lower middle upper upper middle marten- lower of 0. 001%/hr (psi) bainite pearlite pearlite bainite bainite site pearlite 20,000 17,000 16,500 16,000 15,000 15,000 10,000(d) 22,000 Stress for rupture in lower upper middle marten- middle upper lower 1000 hours (psi) bainite bainite bainite site pearlite pearlite pearlite 20,000 18,000 18,000 18,000 17,500 17,500 13,000 18,000 1200 Stress for 1. 0% total upper middle middle lower marten- lower upper deformation in 100 pearlite bainite pearlite bainite site pearlite bainite hours (psi) 14,000 13,000 12,000 11,000 9,000 8,000 7,500 16,000 Stress for rupture in upper middle middle lower lower upper marten100 hours (psi) pearlite bainite pearlite bainite pearlite bainite site 17,000 16,500 15,000 14,500 14,000 13,000 12,500 17,000 (a) Not determined because of low strength. (b) Extrapolated from time-elongation curve. (c) Exceeded one-percent deformation on loading. (d) Estimated from insufficient data. 39

TABLE XII RUPTURE, TOTAL DEFORMATION, AND CREEP STRENGTHS AT 1100" AND 1200~F FOR TURBINE WHEELS AND ISOTHERMALLY TRANSFORMED BAR STOCK OF H-40 STEEL Rupture Strength One-Percent 0. 001%/Hour Structure __ (psi) _ Total Deformation Creep Strength Strength(psi) 100-hr 1000-hr 100-hr 1000-hr (psi) 1100~F Pearlite Bainite (43,000) 30,500 35,000 22,000 25,000 Oil Quench. Barstock 42,000 29,000 35,000 23,000 25,000 Norm. Barstock 41,000 29,000 39,000 28,000 31,000 Oil Quench. Disk 48,000 32,000 42,000 31,000 34,500 Norm. Disk 45,000 32,500 Int. Quench Disk 47,000 30,500 1200~F Pearlite 26,000 Bainite 24,000 Oil Quench. Barstock 23,000 Norm. Barstock 25,000 - Oil Quench. Disk 30,000 ( ) Indicate approximate values. 40

TABLE XIII RUPTURE, TOTAL DEFORMATION, AND CREEP STRENGTHS AT 1100F FOR TURBINE WHEELS AND HEAT TREATED BAR STOCK OF C-422 STEEL 0. 001%/hr Rupture 1.0% Total Deform- Creep Structure Strength (psi) ation Strength (psi) Strength 100-hr 1000 -hr 1-hr 1 000-hr (psi) 1100'F Oil-Quenched -- -- -- 30,000 Bar Stock Normalized (44,000) 34,000 36,000 29,000 31,000 Bar Stock Oil-Quenched 43,000 36,000 36,000 30,000 32,000 Wheel Normalized 39,000 32,000 32, 500 (28,000) 30,000 Wheel ( ) Indicate approximate values. 41

TABLE XIV CHEMICAL COMPOSITION OF FORGED TURBINE WHEELS Type C Mn Si P S Cr Ni Mo V W Cu Manufacturer's Steel (%) (%) (%) (%) (%) (%) (%) (%) (%) (%) (%) Heat Number 4340 0.40 0.76 0.29 0.010 0.015 0.74 1.91 0.50 - - - 656601 "17-2ZA"S 0.30 0.57 0.60 0.018 0.019 1.22 0.23 0.49 0.24 -- 0.13 38516 H-40 0.29 0.48 0.26 0.012 0.018 3.05 0.49 0.49 0.85 0.55 0.15 K-2509 C-422 0.23 0.81 0.16 0.011 0.012 13.19 0.65 1.03 0.25 0.84 - W-3561

TABLE XV HEAT TREATMENTS OF FORGED TURBINE WHEELS 4340 Steel All forgings were isothermally annealed for 15 hours at 1200*F directly from the forging operation. Surface Brinell Hardness Rim Hub Disk No. 1 - Normalized Forging 1st Treatment: Air Cooled from 1750'F and tempered 2 hours at 1200*F 217 229 2nd Treatment: Renormalized from 1750'F (no tempering) 285 285 Disk No. 3 - Oil Quenched Forging 1st Treatment: OilQuenched from 1750'F and tempered 8 hours at 1200'F 269 255 2nd Treatment: Oil Quenched from 1550'F and tempered at 1050~F 302 285 Disk No. 4 - Interrupted Quench Forging Water Quenched from 1750'F until black, then withdrawn until glow returned. This was repeated until glow did not return upon withdrawal from water. It was then transferred to a furnace at 700'F and held for 8 hours, It was then tempered for 2 hours at 1200~F 302 293 "17-22A"S Steel All forgings were isothermally annealed for 8 hours at 1200*F directly from the forging operation. Surface Brinell Hardness Rim Hub Disk No. 1 - Normalized Forging (a) Air Cooled from 1750F and tempered 2 hours at 1200'F 302 285 Disk No. 3 - Oil Quenched Forging (a) Oil Quenched from 1750'F and tempered 8 hours at 1200'F 302 302 Disk No. 4 - Interrupted Quench Forging (a) Quenched in water until black, withdrawn until glow returned, requenched until black and process repeated until glow did not return. The forging was then placed directly in a furnace at 700F for 8 hours, then tempered at 1200F for2 hours 399 399 (b) Retempered for 2 more hours at 1200~F 341 331 43

TABLE XV Continued H-40 Steel All forgings were isothermally annealed for 8 hours at 1200F directly from forging. Surface Brinell Hardness Rim Hub Disk No. 1 - Normalized Forging (a) Air Cooled from 1950'F and tempered 2 hours at 1200~F 429 444 (b) Retempered 3 more hours at 1200F 341 341 Disk No. 3 - Oil Quenched Forging (a) Oil Quenched from 1950F and tempered 8 hours at 1200F 415 415 (b) Tempered 3 more hours at 1200F 341 352 Disk No. 4 - Interrupted Quench Forging (a) Interrupted Quench from 1950F in water as previously described for other steels; then tempered at 1200F for 2 hours 389 363 (b) Retempered for 3 more hours at 1200~F 341 331 Final Treatments for All Forgings Subsequently, bars cut from all three forgings were retempered for 4 more hours at 1250F 287 to 322 C-422 Steel All forgings were isothermally annealed for 8 hours at 1200F directly from forging. Surface Brirell Hardness Rim Hub Disk No. 1 - Normalized Forging 1st Treatment: Air Cooled from 1900F and tempered for 2 hours at 1200'F 321 331 2nd Treatment: FullAnnealed for 6 hours at 1600'Fand furnace cooled; then air cooled from 1900F and double tempered 2 + 2 hours at 1200F 285 293 Disk No. 4 - Oil Quenched Forging 1st Treatment: Oil Quenched from 1900'F and tempered 8 hours at 1200F 285 285 2nd Treatment: Full Annealed at 1600'F for 6 hours and furnace cooled; then oil quenched from 1900~F and double tempered 2 + 2 hours at 1200'F 302 311 NOTE: Second treatments required due to hard spots after first treatment. 44

TABLE XVI COMPARISON OF MICROSTRUCTURES AND PROPERTIES OF TURBINE WHEELS WITH COMPARABLE STRUCTURES FOR BAR STOCK OF SAE 4340 STEEL AT 1000" AND 1100F Fig- Temp Rupture One-Percent Total 0. 001%/hr Treatment Microstructure ure Strength (psi) Deformation Creep No. (*F) Strength (psi) Strength 100-hr 1000-hr 100-hr 1000-hr (psi) Normalized Wheel Bainite + Martensite 44 1000 48,000 24,000 43,000 17,000 25,000 Interrupted Quench Tempered Bainite + 46 1000 48,000 22,000 46,000 17,000 Wheel Martensite Upper Bainite Bar 70% Bainite + 30% 8 1000 46,000 23,000 29,000 17,000 19,000 Stock Martensite Normalized Bar Stock 65% Bainite + 35% 11 1000 46,000 22,000 33,000 17,000 19,000 Martensite Oil Quenched Wheel Tempered Martensite 45 1000 38,000 15,000 23,000 Oil Quenched Bar Stock Tempered Martensite 12 1000 35,000 18,500 23,000 11,000 12,000 Normalized Wheel Bainite + Martensite 44 1100 18,000 -- 11,000 Interrupted Quench Tempered Bainite + 46 1100 19,000 -- 15,000 Wheel Martensite Upper Bainite Bar 70% Bainite + 30% 8 1100 18,000 Stock Martensite Oil Quenched Wheel Tempered Martensite 45 1100 16,000 (6,000) Oil Quenched Bar Stock Tempered Martensite 12 1100 (14,000) -- 9,000

TABLE XVII COMPARISON OF MICROSTRUCTURES AND PROPERTIES OF TURBINE WHEELS WITH COMPARABLE STRUCTURES FORBAR STOCK OF "17-22A"S STEEL AT 1100' AND 1200F Fig- Temp Rupture One-Percent Total 0. 001%/hr Treatment Microstructure ure Strength (psi) Deformation Creep No. (*F) Strength (psi) Strength 100-hr 1000-hr 00-hr 1000-hr (psi) Normalized Wheel Pearlite + Ferrite + 48 1100 35,000 15,500 -- -- Bainite Lower Pearlite Bar 40% Pearlite + 60% 15 1100 30,000 13,000 22,000 Stock Ferrite Oil Quenched Wheel Tempered Bainite + 49 1100 41,000 19,000 36,000 17,000 21,500 Martensite O~ Interrupted Quench Tempered Bainite + 50 1100 42,000 22,000 -- Wheel Martensite Lower Bainite 100%FOO ne Acicular 18 1100 40,000 20,000 33,000 17,000 20,000 Bainite Middle Bainite 97% Fine Acicular Bain- 17 1100 39,000 18,000 30,000 15,000 15,000 ite + 3% Martensite Normalized Bar Stock 85% Coarse Bainite + 20 1100 44,000 18,000 (34,000) 18,000 22,000 15% Martensite Oil Quenched Wheel Tempered Bainite + 49 1200 14,000 -- 11,000 Martensite Lower Bainite 100% Fine Acicular 18 1200 14,500 6,700 11,000 Bainite Middle Bainite 95% Fine Acicular Bain- 17 1200 16,500 7,000 13,000 ite + 3% Martensite Normalized Bar Stock 85% Coarse Bainite + 20 1200 17,000 7,200 16,000 15% Martensite

TABLE XVIII COMPARISON OF MICROSTRUCTURES AND PROPERTIES OF TURBINE WHEELS WITH COMPARABLE STRUCTURES FOR BAR STOCK OF H-40 STEEL AT 1100F Fig- Temp Rupture One-Percent Total 0.001%/hr Treatment Microstructure ure Strength (psi) Deformation Creep No. ('F) Strength (psi) Strength 100-hr 1000-hr 100-hr 000hr (psi) Oil Quenched Wheel Tempered Bainite + 53 1100 48,000 32,000 42,000 31,000 34,500 Martensite Interrupted Quench Tempered Bainite + 54 1100 47,000 30,500 Wheel Martensite Normalized Wheel Tempered Bainite + 52 1100 45,000 32,500 Martensite Bainitic Bar Stock 100% Bainite 22 1100 (43,000) 30,500 35,000 22,000 25,000 Normalized Bar Stock 80% Bainite + 20% 24 1100 41,000 29,000 39,000 28,000 31,000 Martensite

TABLE XIX COMPARISON OF MICROSTRUCTURES AND PROPERTIES OF TURBINE WHEELS WITH COMPARABLE STRUCTURES FOR BAR STOCK OF C-422 STEEL AT 1100F Fig- Temp Rupture One-Percent Total 0.001%/hr Treatment Microstructure ure Strength (psi) Deformation Creep No. ('F) Strength (psi) Strength o00 ______ _________ ____ 100-hr 1000-hr 1hr1000 (psi) Oil Quenched Wheel Tempered Martensite 59 1100 43,000 36,000 36,000 30,000 32,000 Normalized Wheel Tempered Martensite 58 1100 39,000 32,000 32,500 (28,000) 30,000 Normalized Bar Stock Tempered Martensite 26 1100 (44,000) 34,000 36,000 29,000 31,000 Oil Quenched Bar Stock Tempered Martensite 25 1100 - -- 30, 000

1700. 1600 1500 ——. —-- 1400 1300 - 1200 ---- — nite + Ferrit AUST NITl I I X X YFerrite arbide AUSTENITE 1100 0 - H 900 ----,5 1 1000 -ii100, Figure 1. Time-Tempera e Austenite + Ferrite +or 3bid 700 errite + Carbide 600 Ms 500....I 5 10 100 1000 10,000 100,000 Time, seconds Figure 1. Time-Temperature Transformation Curves for 4340, Austenitized 1550~F, Grain Size, 7/8. (Atlas of Isothermal Diagrams, United States Steel, 1951.)

1700 —----- 1400 - --- - 1300 -e - Austenite + 1,I 1 errite + Ferrite + Carbide Carbide 1200 USTENITE.T -mm F 1100 -m- -r Ca g 1000 - I I I 900 --- - Austenite +Ferrite +Carbide 800 -- Ferrite + Carbide 700 —600 500 10 100 1000 10,000 100,000 Time, seconds Figure 2. Time-Temperature Transformation Curves for Timken"17-22A"S, Austenitized at 1750F.

1700. —1600 --- ---- 1500 Austenite + Dark Etching 1400 Grain Boundary Precipitate 1300 1200 A - - - USTENIIE - o 1100 L I I __ __. I - - __ _ _ _ i I - _ I I I I 1111 1 r r1 1 _ ^1 C 1100 1 -000 - H 900 - 800 —-- —...Austenite + Ferrite - - 700 --— / Carbide - -- L-lerrite + Carbide 600 —-- 500 10 100 1000 10,000 100,000 Time, seconds Figure 3. Time-Temperature Transformation Curve for H-40, Austenitized at 1950~F.

1700 —---... 1600 150 1400 1AUSTENITE Austenite + Dark Etching Grain __ Boundary Precipitate + Carbides 1300 1200 V C 1100 —--- -- --- 1 000 900 8 1000 — ---- 700 ---- --- 600 —------- 500 -- - -- 10 100 1000 10,000 100,000 Time, seconds Figure 4. Time-Temperature Transformation Curve for C-422, Austenitized at 1900F.

X 1 OOD X 1000D A1i At(||ni~i7 171X1 + 10 he at V 404.| 9o J'N, tA ~d 1. 00 t, 1l BlN Figure 5. 4340 Bar Stock (a) As Transformed to Upper Pearlite and (b) after Creep Testing at 1000OF. 53

X I100D LX 1 OOD ~;-:~::::'' ~~ 11111 &1Q (a) Austienititsd l75O4P + 14 lirs at 115OF- ZZ9 EHN~.:: ~:::a:S aa:I iil a\tB: (b) Austonitized: 1750O 1 + 14 hrs at 115O~F + creep tested 153-9 hrs at 10000fFx and 1 3,}000 i~i -I 33 BHN. - Figure 6. 4340 Bar Stock f(a) as Transformed to Middle Pearlite and (b) after Creep Testing at 1000~F 54

XIOOD X1000D::i::: ~: i:i: i i i: i i:i:~:::::::::::1 5::::::::11 i i:: i i~:::11 i~ i:i:~::i:::::::::: ~: ~1:~: x i:i i: i: i:: i::: 1 i:~:i:i: i:i~ i::: i i::::::::::~:i:i i:i i:::i::::::::i:~i:~i::::::: i:i::i 11::::i::i 11::: i 1 1:i:: ~i:: 1 1:::~i-i:::i::i -i::i i:::: i:::::::::1:1::::::: i:i::: i::~:i:::~::::::::::::::::::,:::::::%::::::: ~:::::::::::::~::::::~::::::3 113 l iiii i l iif-:::::::::::,: i~~ ~ 9::::::::~::::::::::::::::::,:::::~:::::::::::::.::~::::,:::,:::::::::::,:::::::::::::::::::,:::~::::::::~::::~::::,:::::::::::::r::::::::::~: i- - - -l ii:i~: ~: i:i:: - -:::::::::: ~::::: ~::~:::::::::::::::::~:::::~:::~::::::::::::::::::::::::::::~ ~:::: ~:::: (iue7 30 a tc a) AssTranstormed 110Fo 1 howr Periead 1OOF Z0bHN after'7ii_~_ * C e-Rupt: Test::ing at 000~ I::-::-: —:- I-::::5 5 A ~ ~ ~ ~ ~:::~ —-,_::::,-~::::1~::: 1k. IV.Qib~~l~ L:2~'~:i~\::i~j:::_ L i,:~;:Z-i~::: ~ - ii~~~,n ~;ill~.~l -_::::::::::: 14 ~ ~ ~ ~'ii~i::r.'-_-:::-_i:~ I:::,i::::::~j:\:::::::~Li:~iiii::i::4ii_:~:-: ~ u~::::::::d::::-:-_\~~~~~~~~~4/4* ~~~~~~~~~~~~~::::::::: I':-::..r::: (b) Austcniti~~~~ied 17 O~~F 4 111 hrs at 1O5O~~~~F +cree~~rupture testcd 850 hr1 ill at ~ ~ ~ ~ ~ ~~~:::::::: 100:1 and 13,000~ pn~ aio $BN~iiii~jljljllj Wigure 7. 4340 Bar Stock (a) As Transformed to Lower Pearlite and (h): aferCre Rupture~j'j~:ii,:S::.~; Testing::::::::::::::::: at 1000 5 5~s:,~~-,,,,:::::::::::::::::::::::::

X100D X 1000D (az) Austenitize~d 175O0~F + 28 irs a~t 85Ol)F 320 BHN. Figure 8. 4340 Bar Stock (a) As Transformed to Upper Baui~te and (ib) after Creeps Testing at!000~F 56

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X100D X1 OOOD (a) Normalized 17$0~F -:390 flHN.A (c>) ANTk ~ ab) Normabized 17500F + tempered 1 hr ant ll04F -300 BEN 1000~OOF anld Z0,O(000 si 260 BHIN Figure 12. 4340 B~ar Stock {a) As Normalized, (b) As Tempered to 300 BHIN, and (c) after Creep Testing at 1000~F. 60 W~~~~~~ ~~~~~~ LA~~~~gTR A ~ ~ p~~~~~~~I Y-V~ ~ ~~~4J4 M ~ ~ k WS ()Noimalize~C I I7500V + te mpered 1 h at ll00OF + cree tetd 192hsa 1000'IF 411ad 20,000 pi~i 260 BEN.

X100D XIOOOD AQUN O::: o I:~~~~~~~~~~~~:i j:~:,: V~ (.a) A~utenitiz ci 1 75O0 F + 14I/a hlr8 at I3O~ 19/37028+ce~tulu- et 133N: hrs at~~M: 1: hr~ wd1 0C s: At BOVEH# FigAur~e n13t* zed17#2Z75'. i 13a6 S23c 7a BH Nrnfor IN Upe Pali, d ~~xl::X~~ r-'I'* *: -fJl' r7 j)w 1$ 61~~~~~~~~~~~~~~~0 2E. ~~J-:: ~::a E::: w:at- I 00 e p r -; ~ s I~~~ s (jb) l IAu Utcnitihd 17 50E + 4~ r a 3OO + erc~ututc Ited19 hrisat 10Faf(1, 1 9QOOOp~oi~ 21)BHN~ I~gue 3."1~'2"SBa Soc ()AsTrnsoredt Upe Pealt, n (b) after Greep~upture Testing at 1100 61~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~~*

X100D X1000D (a) Austenitized 1 1750F + 1-1/2 hrs at 1225*F - 85 BHN: 1100*F ad 9,000 psi 259 BHN. Figure 14. "17-22A"S Bar Stock (a) As Transformed to Middle Pearlite and 6Z

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X100OD X1I000D Al 45 i~~~~~~~~~~~~~~~~O: olp ~~ ~~r I ~~~~~ 44X!Bet hle he ",.:".4 ~.07 (a)~I No rrahlzed! 19000F 4 85 BHN. A, ~ ~ ~ ~ ~ ~ ~ ~ A ~~~~~~~~~~~'~ ~ ~~~~~~A ( Northaiz~ed F90~ +Rtonpered ~24 hr s at 1200 OF 302l BII A ~~~~~~~~~AW 366hr, WI 10' ad3,0 pi21BN oianzd ()afe Creep. j~ptured: Testing atMO r11000F.'O ~ ~ Z 8 1 74

100,000. 80,000 ____ ^^_______..____ 60,000 6,0 - Normalized Wheel' 1_ ____ - -. — Int. Quench Wheel | - - -- 40, 000 40,000 ----— Oil Quench Wheel a Upper Pearlite 30,000 4 Middle Pearlite 0I I I I 1 4 |X -- A Lower Pearlite'' o Upper Bainite 20 000 - Middle Bainite I _o a - * Lower Bainite 0 Normalized Bar Stock X Oil Quenched Bar Stock 10,000 I I! 4] (' 2j 50,000..... 7 7_.... -. 40,000 4i0-0 0 0 | c _ l l | | | | | | 1 1(0 0"F 30,000 _i _ _' - 20 000 10,00000 1000 1 10 100 1000 Time, hours Figure27. Comparison of Stress-Rupture Data at 1000~ and 1100~F between Isothermally Transformed Structures and Variously Heat Treated Turbine Wheels of SAE 4340 Steel.

~~~~~~~~~60,' ~~~~~~~~000 ~~I00' 4,1 1000 - 50,000 -- 40,ooo 000 30,000 -' | 1 —0 lt. Quench Wheel z o.|~ ~ ~ ~ ~ ~ ~~~~ ooo~ ~ ~ ~~~ ~~ t _]]lll ll|||4 Middle Pearlite 210,000 -------- ------------— e —------------------ ------ Bo 0'"(0 ~ ubieWel fSA 30Sel u3 CO 10,000 a __ Upp_ 3_______ i1^^1 1| ~~~~~~~~~~~~ —-- Normalized Wheel 0.''-^ 1.0 1100F - Int. Quench Wheel Turb —-Oil Qench Wheels of SAE 4340 Steel. ^^^^^^ t A Upper Pearlite'^^^'^><^^^ -^ ^ Middle Pearlite ^"' -....^^^..;..,_ &"^,^ A Lower Pearlite [^" [^ ss^^^1 |'"''^ 0 Upper Bainite 20,000 -------- ---- --- -- - - ->-^ ^ ---- ---- --- -- — ~> ^ ^- > ^ -^ ---- --- -- - _ _ __ ------------ -- () Middle Bainite - ~ Lower Bainite "^> -— ^^ ^^^^~^ <''llt *^. 0 Normalized Bar Stock X Oil Quenched Bar Stock 10,000 0. 1 1.0 10 100 1000 Time, hours Figure 28. Comparison of 0. 5-Percent Total Deformation Data at 1000~ and 1100~F between Isothermally Transformed Structures and Various Heat Treated Turbine Wheels of SAE 4340 Steel.

60,000 I. 1000'F 50,000 j -. 1_ _ 40,000 4,0 _i__ l _Quench Nheel l l l 1 ____S _ ____ __ ____ -_ _______ __ 40,000 I ~ iz rS F 3 ---- ---- -nt. QuenchWheel 1100*F O.1000Oil Quench Wheel 1 1 1 0 30, 000 a Upper Pearlite 4 Middle Pearlite 20, oooMiddle Bainite -- Normalized Bar WheelStoc 10, 000 1100~F. --- - Oil Quench Wheel -1000 30,000 - AT Upper Peated Turbine Wheels of SAE 4340 Steel. 4 Middle Pearlite ~ Lower Pearlite D Upper Bainite I I ^ *s 20,000 _ Middle Bainite _ I * Lower Bainite X r 0 Normalized Bar Stock X Oil Quenched Bar Stock 10,000 0. 1 1 10 100 1000 Time, hours Figure 29. Comparison of One-Percent Total Deformation Data at 1000~ and 1100~F between Isothermally Transformed Structures and Variously Heat Treated Turbine Wheels of SAE 4340 Steel.

70, 00050,00 _ 40010000~F 40, OO.-_ — -------- I 30,000 -. 20,000 0 - - - -- - - 0;- - - - 4 - =-= i-.i R _o, o o o..... _..-_-. o I- I I _I,_.._.__._._____. 0 Normalized Bar Stock.0 1 "~ I / - Normalized Wheel m ~ _-J I a ~! i~~ I --- Int. Quench Wheel 000 LLJ111 L I Do I _/I I I 1;: I>j,,.. - --— Oil Quenched Wheel 0 4 0 "A4 x I - o100 to m I o _ a Upper Pearlite 3 000 I IO O I- I I I — 1 ---- _ —- Middle Pearlite 8,. 00001.001.01.1 w 8,000 _ _1 ( I- -- ___________ ___ __ _ _ _~-_ _______^ ___ __ _ _- --. _ ~ Lower Pearlite _ _ _ _ _______C__ ___ __ _ _ __^_ ___________0 Upper Bainite, % /hour Fir6,0.Comparison of Stress - Creep Rate Data at 1000 and 1100F between Isothermally Lower Bainite -------- --- -- — Heat Treated Turbine0o Normalized Bar Stock ^0Od ( * X I X Oil Quenched Bar Stock 4,000 3,000 -- 0.0001 0.001 0.01 0.1 Creep Rate, %/hour Figure 30. Comparison of Stress - Creep Rate Data at 1000~ and 1100~F between Isothermally Transformed Structures and the Variously Heat Treated Turbine Wheels of SAE 4340 Steel.

3000 k 0.0015 - 0 t 30 0005 700'F l Minimum Creep Rate at 700F I 90, 000 psi aV A 2000 0.0010 E1 I 1000 3 0.0005 -/\ orml-.R / \ /^^^-~- Normal3'iA ized Bar 0 *^..J\'./" Stock Q.0_. r Q SokTime for 1. 0% Total 0 Oy l~~ *' / Deformation at 90,000 3000 0. 0015 -- - 0 9000F I' t Minimum Creep Rate at 40, 000 psi Go * —-- ~ A 12000 0.0010 -- o 0 \ | Norm lized ~~~ L- - -— \ / IooBar 6Eo ~~ OS~~~~~~ WStock 1000 0. 0005 -Time for 1.0% Total Trnsorato Tme, *\/Deformation at 40,000 \./\ / P, Oi 0ransfor/ ed StrtTime for Rupture at 0 —-A / 5,000 psi 0 0't [ 50,000 1000'F Norm(NOTE:40,000 Propes of alized 40,000 _0_ - Bar- Stock 0-0! /\/ Stock:to teprtueye30,din o o o r ms sa 100-Hour Rupture Strength 7 \/ 9 0 1.0% Total Deformation in / \ I/ O/100 Hours 20,000 1000 20.000,x,- \' -- ~~ 0 -Q ur Rupture Strength %-\ I *7j 1000 Hours 10,000 [ F %A. —-— & 1.0%/o Total Deformation in!0,000 i 0000 n I Normal100ooF z ei0f,,- d Bar [ —.." Stock 0 I |'a" //~ D0 0100-Hour Rupture Strength 10,000 A- \C / ^1. 0% Total Deformation in'' A7" 100 Hours A ~jS 1Al. 0% Total Deformation in -. W K'.1A 1000 Hours 0 --- -I I I___I I_____________ 600 800 1000 1200 Transformation Temperature, *F a a) a S~~I ~ a,^~ ~~ a Transformed Structure Figure 31. Relationship between Properties at 700~, 900~, 1000., and 1100~F of Isothermally Transformed Structures of SAE 4340 and Temperature of Transformation. (NOTE: Properties of Normalized Bar have been inserted at isothermal transformation temperature yielding structure most similar to normalized bar.) 79 CI k a a a'-4 CIql 0..1 1 4

100,000 80,000 _ __ __ 1100'IF 0, 0000 - - - L- - r T I T —--— _-K- -J 1 111 ___ 60,000 - 40,000 11.O 30,000 Co 10,000 -,1-____ — 1 - --- --- ---— F o;4 40,000 1200'F 3 O, 000 Normalized Wheel | | - Int. Quench Wheel 20,000 - -- Oil Quench Wheel Z Upper Pearlite t Middle Pearlite X O~AnB 4O A A Lower Pearlite 10,n000 0n Upper Bainite I0 4 Middle Bainite 8,000 5 Lower Bainite_ _ 0 Normalized Bar Stock D T x 0 6 000 X Oil Quenched Bar Stock 6,000 1 10 100 1000 Time, hours Figure 32. Comparison of Stress-Rupture Data at 1100~ and 1200'F between Isothermally Transformed Structures and Variously Heat Treated Turbine Wheels for "17-22A"S Steel.

50,000 - -, -- - - - -- - - -- - -- ------- 40,00 0 -L-_L — - - -- 30,000 _ — Normalized Wheel___ ___ ________ 30' -0 -Int. Quench Wheel - - — Oil Quench Wheel I. l A Upper Pearlite I 20 000 Middle Pearlite I -- -- | o A Lower Pearlite^ f F | A | 0 Upper Bainite o | Middle Bainite a O x * Lower Bainite 10, 000 0 Normalized Bar Stock >< Oil Quenched Bar Stock o 0 0O."^^'*'*. I 1200'F 30,000 ------- ---- - - -- "-'- ---- -- — __ ------- ---- -- -- - ---------- -- - 20,000- -- _ XA.4 I o 10,000 -- _-.- - 0. I1 1.0 10 100 1000 Time, hours Figure 33. Comparison of 0. 5-Percent Total Deformation Data at 1100' and 1200'F between Isothermally Transformed Structures and Variously Heat Treated Turbine Wheels for "17-22A"S Steel.

50,000! I I I I - Normalized Wheel Int. Quench Wheel 1100'F --- -- Oil Quench Wheel A Upper Pearlite | | + Middle Pearlite I Lower Pearlite 0 Upper Bainite 30,00 0- Middle Bainite' Lower Bainite o Normalized Bar Stock k Oil Quenched Bar Stock 0,00QO 40,00 Time, hours Figure 34. Comparison of One-Percent Total Deformation Data at 1100 and 1200F betweensothermally Transformed Structures and V Turbine Wheels for "17-22A"S Steel.

100,000 80, 000 - Normalized Wheel - -- - Int. Quench Wheel 60,000 -— Oil Quench Wheel - - - - 1100*F O. -fl 50,000 50000- Upper Pearlite 40,000 4 Middle Pearlite = __ A Lower Pearlite I I I I I I I I I_ ^ 30,000 0 Upper Bainite. -.' _ _ 304000 Middle Bainite — ~C Rt % I Lower Bainite W f I J 2 1200F 5 20, 00,00 O Normalized Bar Stock..- _ 20, 000 - J e, na Stnr -- bOo v, ~~\- oA X0' ~ IO A 10,000 O, — 1' A4. 8,000 __ — - -i [4_ __ ---- - -- _ - 6,000 0. 0001 0. 001 0.01 0.1 1.0 Creep Rate, %/hour Figure 35. Comparison of Stress - Creep Rate Data at 1100~ and 1200*F between Isothermally Transformed Structures and Variously Heat Treated Turbine Wheels for "17-22A"S Steel.

110,00 ( I 700'F 100,000 ——' —-- 2000 4 90,00 oo -\ N / \ \N \ Stress for Creep Rate oQ e / \ }sNor - _ ^of 0.0001% o/Hour wvl~~~~~~~ / \alize 2k ~ / \/ Bar o 1000 80,000 Sock__.5'1~7~ / I Ba \ \ Time for Rupture at 1, 0 70,0oool00 — < / —-_ _D__ _. U1s_ 15, 000 psi H \Bar Time for Rupture at 3,000~ 20,000 ps 9 Barizd\ Time for Rupture at Barnn 70.000 psi _Time for 1.0%0 Total 0, 000'F | 4o. ooo l l * k/0 1.0% Total Deformation in | Normal-'i? I A {~'~-"~O.~ —0Tized Bar 0, 000 I 3 A Stock o oo o /~- | f, 1*00-Hour Rupture Strength 0 A 1. 0%/ Total Deformation in 0/20, ~ - -000 ___ | _ ^, _ -/ _100 Hours A~ r^^A^ | ^ /|~ A 1000 Hours 10,000 _ - 20,000 Normalized IZO12F I stock 3, 100-Hour Rupture Strength Spt ~ ~ ~ 1 D^- ^' A —- --- 100 Hours ~ 10,000 —P/ m A —^ 1 /I g.lO1000l-Hour Rupture Strength 0 * — - - r —I. 600 800 1000 1200 Transformation Temperature, *F ig; O p o 4 A" 10,0 0 1 I p. -S Transformed Structure Figure 36. Relationshipbetween Properties at 700', 900', 1100-, and 1200-F of Isothermally Transformed Structures of "17-22A"S Steel and Temperature of Transformation. (NOTE: Properties of Normalized Bar have been inserted at isothermal transformation temperature yielding structure most similar to normalized bar.) 84 ClT a, ~F 84

100,000 I 80,000 11I____ ___ 60,000 1111 — - -- -....-.... 40,000 CL" 30,000 20a, 000 ~10,000 o 710,000 Bainite Un I IIII50, 000....I IIX 0 a I Normalized Bar Sto _ _0_'l- Int. Quench Wheel 40, 000 30, 000 01 Bainite X Oil Quenched Bar Stock I10 100 1000 Time, hours Figure 37. Comparison of Stress-Rupture Data at 1100' and 1200F~ between Isothermally Transformed Structures and Variously Heat Treated Turbine Wheels for H-40 Steel. (Note: * indicates that specimens fractured in shoulder radius or threads. }

1100'F 60, 000 ~ II o) o 50,000 -- 30,000 - - 00~ ~ ~ ~ ~ ~ 100 30,000 —- _ —l — I IEii O3II ~ ~ X - - - l Oil 40, 5-Percent Total Deformation Data at 1100 and 00F between Isothermally Transformed Pearlite 0 Turbine Wheel of H-40 Steel. 0 Normalized Bar Stock Oil Quenc 30, 000 - - 20, 000 - e Wheel 0. 1 1.0 10 100 1000 Time, hours Figure 38. Comparison of 0. 5-Percent Total Deformation Data at 1100. and 1200~F between Isothermally Transformed Structures and an Oil Quenched and Tempered Turbine Wheel of H-40 Steel.

60, 000 IIlOO'F 50,000 - -— Oil Quenched Wheel a Pearlite 40, 000 --- o —----- ---- --- ---------- ---- -- ---.0 oD Bainite o Normalized Bar Stock ^ O CO_ 30, 000 X Oil Quenc hed Bar Stock l 20,000 - - 10,000 00 0 0. 1 1.0 10 1000 Time, hours Figure 39. Comparison of One-Percent Total Deformation Data at 1100" and 1200F between Isothermally Transformed Structures and an Oil Quenched Turbine Wheel of H-40 Steel.

100,000 80, 000 60,000 _ - 40,000 -,o' 1.X 00 __________ o Oil Quenched Bar Stock 10,000 10,'000 _I I Io _ —--- -— I I 0. 0001 0.001 0.01 0.1 1.0 Creep Rate, %/hour Figure 40. Comparison of Stress - Creep Rate Data at 1 100 between Isothermally transformed Structures and an Oil Quenched and Tempered Turbine Wheel of H-40 Steel.

100, 000 80,000 60,000 ---- Normalized Wheel ------ 40,000 Whee 40000 -- -— Oil Quenched Wheel 30,000 --- Normalized Bar Stock ---- -- - -- ---- -- - -- -- --- -- - -- — O 5 X Oil Quenched Bar Stock 00 G 20,000 10,00001 i.0 10 100 1000 Time, hours Figure 41. Comparison of Stress-Rupture Data at 1100'F between Normalized and Oil Quenched Bar Stock and Variously Heat Treated Turbine Wheels of C-422 Steel.

60,000 -..... 50,000 1100"F 40,000 - - 1-. ND S 30,000 --- -- - - _ —-- - -- - - - _ ---------- -- - - - ii L O X --- ---- [ -- l - Tp O C X 3 -— Oil Quenched Wheel' 10 0 Normalized Bar Stock 0 5% X Oil Quenched Bar Stock 20,000 --- 10,000 0. 1 1.0 10 100 1000 Time, hours Figure 42. Comparison of 1.0- and 0. 5-Percent Total Deformation Data at 1100~F between Normalized and Oil Quenched Bar Stock and an Oil Quenched and Tempered Turbine Wheel of C-422 Steel.

100,000 80,000 1 1 -- - 60,000 _________ - -- - Oil Quenched Wheel 1100'F 40,000 0 Normalized Bar Stock -' 3 )C Oil Quenched Bar Stock o - - 30,000 ----- 20 000 10,000 0. 00001 0. 0001 0. 001 0. 01. 1 Creep Rate, %/hour Figure 43. Comparison of Stress - Creep Rate Data at 100-F between Normalized and Oil Quenched Bar Stock and an Oil Quenched Turbine Wheel of C-422 Steel.

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