ELEVENTH PROGRESS REPORT TO MATERIALS LABORATORY, WRIGHT AIR DEVELOPMENT CENTER DEPARTMENT OF THE AIR FORCE ON FOUR LOW-ALLOY STEELS FOR ROTOR DISKS OF GAS TURBINES IN JET ENGINES R. L. Jones A I. I. Ruse J. W. Freeman PROJECT M903 AIR FORCE CONTRACT NUMBER: AF33(038)-13496 SUPPLEMENTAL AGREEMENT NUMBER: S4(53-534) EXPENDITURE ORDER NUMBERS: 605-227 SR-7 and R615-13 SR-3a September 30, 1953

SUMMARY This report presents the progress made in an investigation of the high temperature properties of low-alloy steels for use in jet engines. The period covered by the report was from July 1, 1953 to September 30, 1953. Nearly complete data are submitted for survey tests of the influence of type of structure on properties at temperatures ranging from 700~ to 1200~F for three steels. The steels are 4340, "17-22A"S and H-40 steels. The structures being considered are those obtained by isothermal transformation of 4340 and "17-22A"S at three peratures in the pearlitic region and three in the bainitic region. In addition, normalized and oil-quenched specimens are included. The data to date tend to show that as the test temperature is increased, maximum strength is associated with increasing temperature of transformation. Thus for 4340 steel, maximum strength shifted from lower bainite to upper bainite and the pearlites as the test temperature was increased from 700~ to 1100~F. A similar, but less clear cut, trend was shown for the "17-22A"S and H-40 steels. The high strength of normalized steels is dependent on bainite formation. Apparently considerable variation in the strength of normalized steel is possible, depending on the type of bainites formed. The relatively high strength of the normalized specimens over the entire range of temperatures is probably due either to range of bainitic structures or to an advantage from continuous cooling transformation in the bainitic region. Certain apparently anomalous relationships between structure and properties, particularly for "17-22A."S, need further clarification.

2 INTRODUCTION This report covers the work done during the period between July 1, 1953 and September 30, 1953 on an investigation of the metallurgical factors involved in the use of heat-treatable low-alloy steels at high temperatures in aircraft propulsion systems. Contract Number: AF 33 (038)-13496 (Expenditure Order Number: 605-227 SR-7) and Supplemental Agreement Number: S4 (53-534) (Expenditure Order Number: R 615 -13 SR-3a) authorize the work. The investigation first evaluated the high temperature properties of four low-alloy ferritic steels in the form of rotor wheels for jet-engine gas turbines. A concurrent, limited investigation was started to determine the realtionships between types of structure, as controlled by heat treatment, and properties of the alloys. The properties of such steels at elevated temperatures vary with the types of structure formed by heat treatment as do the ordinary room temperature properties. The relationships between structures and properties at high temperatures are, however, not known. For this reason, that phase of the work was extended and is the subject of this progress report. Nearly "pure structures" are being made by isothermal transformation of three ferritic steels: 4340, "17-22A"S and H-40. The properties of these steels after transformation under controlled conditions are being surveyed at temperatures ranging from 700~ to 1200~F by limited creep and rupture tests. The initial surveys are nearly complete for this report. Immediate work for the future will involve completion of the isothermal studies and extension to include various rates of continuous cooling transformation. The final objective is to establish the metal

3 lurgical principle for producing as nearly optimum properties at elevated temperatures as possible in such alloys under production conditions. TEST MATERIALS The chemical composition of the alloys being studied was reported by the manufacturers as follows: Steel Heat C Mn Si Cr Ni Mo V W 4340 19053.40.70.30.78 1.75.26 "17-22A"S 24797.30.63.60 1.25.25.52 o25 "17-22A"S 10420.29. 61. 67 1 30.18.47.26 H-40 K-2509.29.48. 26 3.05.49.49.85 55 In extending the study of structures and properties, it was necessary to obtain additional bar stock. Additional stock of 4340 steel was obtained from the same heat as originally used. It was, however, necessary to take additional stock from another heat of '17-22A"S steel. The original supply of H-40 bar stock was sufficient for the purposes of the additional work. RESULTS The structures obtained by the heat treatments are outlined in Tables I, II and III. It will be noted that isothermal transformations were carried out at three temperatures in the pearlitic region and at three temperatures in the bainitic region for 4340 and "17-22A."S steels. One temperature of transformation was used for each region for H-40 steel, due to limited transformation characteristics of this higher alloyed steel. The temperatures and times of transformation were based on

4 time-temperature-transformation diagrams previously reported. In addition, the structures obtained by the usual oil quenching and normalizing operations have been carried along. It is important to recognize, as is outlined in the tables, that the actual structures deviated from the Idealized structures in some cases. Simple names referring to the idealized structures have been used in referring to treatments and structures in the text as a matter of convenience. It should be further recognized that the idealized names do not necessarily describe the same structure in all steels. The names more accurately reflect the position of the transformation temperature in relation to the time-temperature-transformation diagram than the actual microstructures. Under many conditions of transformation, the time for complete transformation was very long. Furthermore, the transformation rate often became so slow as to virtually stop before complete transformaion. In such cases, the treatment conditions were selected to produce a predominance of the aim structure and to subsequently quench out the remaining austenite to martensite. In those cases where the initial hardness exceeded 320 Brinell, tempering was used to reduce the hardness to 280-320 Brinell. Tempering curves have been previously reported. Typical microstructures of the as-transformed structures are shown in Figures 1 through 20. The average percentage of each type of structure, based on a number of observations, has been included in Tables I, II and III. The tempered structures are not shown at this time because tempering tends to obscure the actual structure obtained by transformation. As previously mentioned, however, the structures harder than 320 Brinell were tempered before testing.

5 Survey of Properties of Structures at Elevated Temperatures In setting up the original program for evaluating structures, it was decided to proceed on the following general basis: 1. Evaluate properties of structures over the range of temperatures over which creep could be a factor in performance. The lower limit was set at 700~F and the upper limit at 1100~F for 4340, and 1200~F for "17-22A."S and H-40 steels. 2. As the temperature is increased, the stresses at which yielding occurs shift from below those at which rupture occurs by creep in reasonable times to being well above the rupture strengths. For this reason, creep is the major factor of interest at 700~F. Any stresses causing rupture in less than 1000 hours would be well above the yield strength and yield characteristics would limit service stresses to those below which rupture would occur. Attempts were made to find a single stress which would evaluate the structures on the basis of the time required to reach one-per cent total deformation, At 900~F, the intent was to also evaluate structures on the basis of total deformation, using a single stress. At 1000~F, testing was limited to 4340 steel. Both creep and rupture properties were considered of interest at this temperature. It was considered, however, that two different stress levels would be required to evaluate both properties satisfactorily. The same reasoning was used for "17-22A"S and H-40 at 1100~F. Testing at 1200~F was limited to "17-22A"S and H-40 steels. At this relatively high temperature, rupture properties for a time period

6 of 100 hours were considered to be of most interest. 3. In some cases, the initial stress chosen was not well suited and repeat testing at another stress became necessary. This also arose in some cases from the choice of stress in the early part of the work where only the stress for one-per cent deformation was considered in the evaluations. As discussed later, the range in strength of the structures in some cases was too wide for evaluation by a single stress and recourse to variable stresses based on a percentage of the yield strength will be used for evaluation. Survey of Relationships between Structure and Strength for 4340 Steel The data obtained during the period covered by this report are given in Table IV. All of the data obtained to date have been summarized in the form of bar graphs in Figures 21, 22 and 23 to show the general trends of the data. 1. Properties of 4340 at 700~F: Minimum creep rates and the time required to reach one-per cent total deformation summarized in Figures 21 and 22 indicate that maximum strength was associated with the normalized structure and with structures formed at temperatures just above the martensite reaction temperature. There may have been some added contribution from continuous cooling transformation as judged by the high strength of the normalized stock. The higher the transformation temperature, the lower the strength. Actually, tle pearlites are not being well evaluated by the stress used because their ultimate strength was so low, due to low hardness, that fracture occurred shortly after applying the load.

7 Tempered martensite obtained by oil quenching did not have as good creep resistance as the bainites or normalized material. This was an unexpected finding in that it had heretofore been expected that tempered martensite would compare more favorably at a temperature as low as 700~F, 2. Properties of 4340 at 900~F: Rupture of all the samples occurred in 4. 5 to 1417 hours under 55,000 psi (see Figures 21, 22 and 23). Increasing the temperature of testing from 700~ to 900~F apparently raised the optimum temperature of transformation to that of middle bainite. Lower bainite and the normalized material were even weaker than the upper bainitic sample. As expected, tempered martensite was comparatively weak. Again, the pearlites compared unfavorably due, at least in part, to low hardness and the relatively high testing stress. The low elongations of the high strength middle and upper bainites in comparison to the other structures should be noted. 3. Properties of 4340 at 1000~F: Initial tests were carried out at 13, 000 psi with the results summarized in Figures 21 and 22. The optimum strength again shifted to a higher temperature of transformation, upper bainite, with increasing test temperature. Upper and middle pearlite compared more favorably than at the lower temperatures. Lower pearlite was, however, the weakest structure tested. Tempered martensite fromoil quenching and lower bainite were quite weak. Because 1000~F is a relatively high testing temperature for 4340 steel, relatively short time - high stress properties are of sufficient interest to warrant further study. For this reason, the structures are being tested at 31,000 psi for rupture strengths. Two such test results are included in Figure 23. While the data are limited, it will be

8 noted that the upper bainite sample was stronger than the rmiddle bainite, as in the lower stress tests. Figure 23 also includes the results from the one structure, lower pearlite, which fractured under 13, 000 psi. 4. Properties of 4340 at 1100~F: Under a stress of 4500 psi, upper pearlite and upper bainite had the best creep strength (Figures 21 and 22). Middle bainite, middle pearlite and probably the normalized material were next strongest. Again lower pearlite was the weakest. There were some discrepancies between minimum creep rate and total deformation in these rankings. There was also some variation in stress used for the structures. This arose from the attempts during initial work to determine as nearly as possible the stress for one-per cent total deformation in 1000 hours. At 1100~F, higher stress - shorter time properties are again of sufficient interest to warrant rupture tests and such tests are in progress at 18,000 psi. The tests for upper and middle bainite, Figure 23, are included. It will be noted that the difference in rupture strengths was similar to the case for the lower stress creep tests. Survey of the Relationships between Structures and Strength for "17-22A. S Steel Table IV gives the data obtained during the period covered by this report. All of the data obtained to date are summarized to show trends by the bar graphs of Figures 24, 25 and 26. 1. Properties of "17-22A"S at 700~F: The initial sorting stress, 115, 000 psi, proved to be rather high inasmuch as all structures fracture in less than 300 hours, except middle bainite. Middle bainite (197-%o fine acicular bainite) was discontinued without fracturing at 1827

9 hours. It was therefore much stronger than any of the other structures on the basis of all three criteria —minimum creep rate, time to reach oneper cent total deformation, and rupture time. (See Figures 24, 25 and 26.) The next strongest structure was the tempered martensite obtained by oil quenching and tempering. Surprisingly, it was closely followed by middle pearlite. All of the fractured samples had good dutility. The tests at 115, 000 psi did not prove to be very useful in evaluating the structures at 700~F. The stress was too high in most cases, as was evidenced by rupture of most of the specimens. Secondly, there appeared to be a wide variation in strength. At 700~F yield strengths govern the maximum stress which can be used. For these reasons, it is planned to test at a lower stress, using a percentage of the yield strength of each structure as a sorting stress. These tests will also serve as a check on the very high strength shown by middle bainite in the initial tests. 2. Properties of "17-22A"S at 900~F: Middle bainite also had the highest strength at 900~F. (See Figures 24, 25 and 26.) The normalized material was next strongest. Lower bainite, middle pearlite and lower pearlite were the next strongest structures. It is probably important to note that the upper bainite and the tempered martensite of the oilquenched structure were very weak, even in comparison to the middle and lower pearlites. 3. Properties of "17-22A"S at 1100~F: There was a surprisingly small spread in minimum creep rates, time for one-per cent total deformation or rupture time for all the structures under 19, 000 psi. (See Fgures 24, 25 and 26. ) The normalized structure was somewhat the strongest. The individual rankings of the other structures tended to vary, depending on the criterion used. Some of the tests were initially run at

10 20, 000 psi where the objective was to obtain fracture in about 1000 hours. All structures had rather low elongation to fracture, except upper and lower pearlite. 4. Properties of "17-22A"S at 1200~F: Although the test is still incomplete, it is evident that upper pearlite will have the best strength at 1200~F under 7500 psi. Middle pearlite and the normalized structure follow in strength. (See Figures 24, 25 and 26. ) Upper bainite, which ranked highest at 700~ and 900~F, was about the weakest at 1200~F. All structures had considerably higher elongation than at 1100~F. Survey of the Relationships between Structures and Properties for H-40 Steel The data obtained during the period covered by this report are given in Table VI. The general trends of all data obtained to date are summarized by Figures 27, 28 and 29. The data for H-40 steel are summarized in Figures 27, 28 and 29. It will be noted that the pearlitic structure was very weak at 900~ and 1100~F, but was slightly the strongest at 1200~F. The sample transformed in the bainitic region was the strongest at 700~ and 900~F and probably at 1100~F. A difference in stress at 1100~F makes the comparison uncertain. The tempered martensites (normalized and oil quenched) showed little difference at any of the temperatures, as might be expected. Probably they will be about as good as the bainitic sample at 1100~F. All fractured specimens showed good elongation.

11 Correlation of Structures of Forged Rotor Wheels and Properties At the time the report on the properties of wheels was submitted, attempts were in progress to correlate the properties of the wheels with their microstructures. This has proven to be very difficult. First, the tempered structures of the wheels are difficult to identify with certainty. Secondly, the information available from isothermal transformation to relate structure to properties has been rather incomplete. It is also turning out that structures formed by continuous cooling, as was the case for the wheels, are difficult to break down in terms of the isothermally formed structures. It has been decided to issue a factual report summarizing the structures of the wheels. Insofar as possible, the structures will be related to properties. However, a good correlation will be dependent on the completion of the study of the continuously cooled structures now in progress. DISCUSSION The initial surveys of representative structures formed by isothermal transformation are nearing completion, While the data are sparse, certain trends are becoming evident. 1. There is a definite trend for maximum strength of 4340 steel to be associated with increasing temperature of transformation as the test temperature is increased. A similar trend is present for "17-22A"S steel, although less definite than for 4340 steel. H-40 steel

12 reacted in the same way, as judged by the shift in relative strengths of the "pearlitic" range and tempered martensites. In all three cases, bainites tended to have the highest strength, although for 4340 and "17-22A"S there was considerable variation, dependent on the temperature of transformation within the bainitic region. 2. For 4340 steel there was a definite progression of maximum strength with increasing temperature from 700~ to 1100~F. At 700~F, transformation just above the Ms temperature was strongest. The Cr-Mo-V steels ("17-22A"S and H-40), however, apparently varied somewhat in transformation conditions for maximum strength at 700~, 900~ and 1100~F. At the highest temperatures (1100~ or 1200~F) in every case pearlitic range transformation tended to give highest strength. This correlation between temperatures of transformation and properties does take into account the relatively high strength of the normalized structures. It is assumed for the present, at least, that normalizing of 4340 and "1t7-22A"S produces transformation over a range of temperatures in the bainitic region. Thus, the normalized structures tend to include the most favorable temperatures of transformation and have high strength over a considerable range of test temperatures. There also seems to be reason to believe that there was an advantage for continuous cooling transformation during normalizing at some test conditions. It is not certain, but probable, that secondary hardening effects introduced by vanadium influence the strength characteristics of the "17-22A"S and H-40 steel. This probably is related to the apparent non-uniform relationships between types of structures and strength in comparison to the regular progression for 4340 steel.

13 3. The differences in strength between structures tended to diminish with increasing testing temperature. 4. Because normalizing or liquid quenching are almost universally used for practical heat treating, the indications of the data for these treatments are important. Heretofore it has been thought that tempered martensite would be at least equal to other structures at relatively low temperatures. However, intermediate transformation products have shown better properties for all three steels at the lower temperatures. For 4340 and "17-22A"S steel, tempered martensite did fall off very rapidly with increasing temperature. However, it did retain its strength very well for H-40 steel up to 1200~F. Normalized structures have generally been noted for their relatively high strength at elevated temperatures. In general, normalizing did tend to give relatively high strengths. It seems evident, however, that the strength after normalizing will be dependent on the cooling rates which control the temperatures of transformation and the resulting structures. In other words, the normalized specimens tested have strengths characteristic of transformation of one-inch bar stock on air cooling. Other section sizes would cool at different rates and transform differently as a consequence. This should modify the relative position of "normalized" structures in the rankings shown. 5. It should be noted that while pearlites tend to become strong in relation to the other structures at 11000 and 1200~F, "upper" pearlite seems always to be the strongest. Lower pearlite was very weak in most of the tests.

14 6. There was some variation in hardness between the structures and between the same structures tested at different temperatures. The following tabulation gives the hardness data obtained on the individual specimens of 4340 steel before testing. S? a Test Temp Stress c ~ a c ~ ~.1-i 0 0 (~F) (psi) _ d N U 700 90,000 -- 199 -- 324 309 277 300 304 900 55,000 217 231 260 325 313 277 300 306 1000 13,000 219 229 270 322 307 294 301 306 31,000 -- -- -- 327 295 -- -- -- 1100 4,500 212 233 275 319 302 301 311 309 18,000 -.a - 233 293 -... _ Reference to the creep-rupture data shows that: (a) Lower bainite had superior strength at 700~F in spite of lower hardness. The test temperature had to be increased before the higher hardness middle and upper bainites became superior. This is contrary to the expected trends of higher hardness accompanying higher strength, the lower the test temperature. (b) In view of the differences in strength, it is unlikely that lower bainite with an equivalent hardness would have equaled the strength of middle and upper bainite at the higher test temperatures. (c) Upper pearlite, which was much softer than lower pearlite was consistently stronger. The individual variations in hardness, therefore, seem unlikely to be res

15 ponsible for general trends in strength developed previously for the data. The low strength of the lower pearlite seems difficult to understand in view of the hardness. It appears as if the fine carbide structure has inherently low strength. An alternative possibility is that the prolonged time at 1050~F for transformation destroyed some structural condition controlling strength that is not reflected in hardness. As the work continues, more attention will be given to the development of fundamental explanations of the results. 7. The hardness values of the individual specimens of "17 -22A"S steel are summarized in the following tabulation: 4) o MJ, *a a. ' 'a crrTest Temp Stress. l (~ F) (psi) __ __ 700 115,000 -- 267 263 284 309 275 302 278 900 70,000 196 266 266 289 307 283 303 278 1100 19,000 309 285 313 327 310 302 311 306 1200 7,500 237 376 293 320 310 273 318 313 The variations in hardness are considerably greater than seemed reasonable. Checking into the reasons for the tendency for high hardness of the samples run at 1100~F disclosed that in changing heats of stock, a difference in response to heat treatment was found. The microstructures of the newhe at stock (Heat 10420) were originally checked for isothermal transformation characteristics and the two heats found identical for practical purposes. However, it is now known that the two heats

16 vary in as-transformed hardness and tempering characteristics. Heat 10420 tends to give lower hardness on transformation, particularly in the pearlitic region. Secondly, it tempered more easily than Heat 24797. It has now been determined that tempering conditions should have been changed as follows to obtain 300 Brinell hardness: Heat Number 24797 Heat Number 10420 Temp Time Temp Time (~F) (hrs) (~F) (hrs) Lower Pearlite 1200 12 1200 6 Upper Bainite 1200 16 1200 12 Lower Bainite 1200 12 1200 6 Oil Quenched 1300 1 1300 1/2 Future tests will be carried out using the adjusted tempering to keep the hardness values near 300 Brinell. The analyses apparently show no significant difference between the two heats. However the original heat (Heat 24797) had slightly higher C, Mo and lower V. All of these would tend to give high hardenability. The as-quenched hardness of the oil-quenched specimens from this heat are on the high side of the range to be expected for the analysis. Heat 10420, however, quenched out to the lower side of the range. Thus, there is a real difference in hardenability. Secondly, the low hardness of the pearlites from Heat 10420 indicates a substantial reduction in secondary hardening characteristics. Secondary hardening appears to be responsible for high hardness of pearlitic structures in "17-22A"S steel. The influence of these variations in hardness and response to heat treatment on the trends for the relations between structure and properties previously discussed is difficult to clarify. First of all, it depends on which heat is accepted as representative of the alloy. The following comments are offerred: (a) The comparatively high strength of the pearlites at 1100~F may be due in part to high hardness and extensive

17 secondary hardening. This, however, cannot explain their relatively good properties at 1200~F. It seems certain, however, that if the high hardness had been obtained in the specimens tested at 700~ and 900~F, they would have compared more favorably than they did. (b) There are numerous cases where hardness alone cannot explain the variations in strength. It certainly cannot account for the high strength of middle bainite at 700~F or the difference between the oil quenched and normalized samples at 700~F. The same thing is probably true at 900~F for the middle bainite and the normalized materials, although admittedly they both are somewhat harder than other structures. The variations in properties at 1100~F (other than for the pearlites) and at 1200~F do not seem consistent with hardness. (c) It now appears that secondary hardening characteristics are important to strength of "17-22A"S. As yet it is uncertain whether the variation of strength with temperature of transformation is due to heat to heat variations or is related to the effect of the temperature of transformation on secondary hardening. Check tests will be required to clear this us. 8. Thus far, no major variation in hardness has been observed for the H-40 specimens. The variations in strength with transformation conditions, therefore, are free from influence from hardness, other than the low hardening of the sample transformed in the pearlitic region as previously discussed.

18 FUTURE WORK 1. Complete the testing of isothermally transformed specimens as previously outlined in the report. 2. Conduct such check tests as may be necessary to clear up hardness and heat to heat variation effects. 3. Start the study of continuous cooling transformation structures and properties.

TABLE II Type Structures, Heat Treatments and Actual Structures of 1.25 Cr-Mo-Si-V ("17-22A"S) Steel (All I 17-22A"S bar stock austenitized at 1750~F for 1 hour.) Transformation Approximate Structure Tempering Aim Structure Conditions Obtained B H N _Temp-~F Time-hrs T_ Temp-~F Time-hrs Upper Pearlite 1300 1-1/2 45% medium pearlite + 55% 196/237 None ferrite Middle Pearlite 1225 1-1/2 40% medium fine pearlite 266/285 None + 60% ferrite Lower Pearlite 1150 10 40% fine pearlite + 60% 375 1200 12 ferrite Upper Bainite 900 2 60% upper bainite + 40% 465 1200 16 martensite Middle Bainite 800 1/2 97% fine acicular bainite + 360 1200 4 3% martensite Lower Bainite 700 1/12 100% lower bainite 365 1200 12 Normalized Air Cooled from 1750 15% martensite + 85% coarse 355 1200 10 bainite s Oil Quenched Oil Quenched from 100% martensite 525 1300 1 1750 BHN 196/237 266/285 263/313 284/327 307/310 273/302 302/313 272/310

Aim Structure 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 Conditions Obtained B H N ____ Temp-F Ti -hrs Temp~F Time-hrs 1300 24 fine carbide precipitate 190/200 None 750 10 100% bainite 480 1300 1 Air Cooled from 1950 20% martensite + 80% 435 1200 18 Pearlite Bainite Normalized Oil Quenched BHN 190/200 293/313 310/320 290/323 bainites 100% martensite Oil Quenched from 1950 523 1200 12

TABLE IV Rupture, Total Deformation and Creep Data at 700~, 900~, 1000' and 1100~F for 4340 Steel Aim Structure TempBHN erature ( F) Stress Rupture Time (psi) (hours) Elong - ation (% in 2") Reduction of Area (%) Deformation on Loading (in. /in.) Time to Reach Specified Total Deformations 0.1% 0.2% 0.5% 1.0% Minimum Creep Rate (%/hour) Middle Pearlite 199 700 90,000 10.7 23 57 85% fine pearlite and fine carbide-ferrite aggregate + 15% ferrite Middle Pearlite 231 900 55,000 9.7 28 56 a a a <1 85% fine pearlite and fine carbide-ferrite aggregate + 15 %G ferrite Upper Bainite 325 900 55,000 1215 6 6.4 0. 00265 a a 6 48 0.00163 70% upper bainite + 30% martens ite Upper Bainite 327 1000 31,000 389 10 7 0.00185 a <1 13 75 70% upper bainite + 30%/ martensite Middle Bainite 295 1000 31,000 261 5.9 5.6 0.00190 a <1 18 85 100% medium acicular bainite Middle Pearlite 229 1000 13,000 1539(d) -- - 0.00053 10 52 515 1175 0.00060 85% fine pearlite and fine carbide-ferrite aggregate + 15% ferrite Upper Pearlite 212 1100 4,500 1146(d) -- -- 0.00053 52 235 893 1900(b) 0.00046 65% medium pearlite + 35% ferrite Middle Pearlite 233 1100 4,500 1148(d) -- -- 0. 00024 25 93 315 643 0. 00139 85%1 fine pearlite and fine carbide-ferrite aggregate + 15% ferrite Middle Bainite 293 1100 18,000 80 11 8 0. 00080 100% medium acicular bainite Upper Bainite 323 1100 18,000 106 14.3 10 0.00130 70% upper bainite + 30% martensite (a) Specimen reached this deformation on loading. (b) Extrapolated value. (c) 0. 250-inch diameter specimen, elongation % in 1-inch. (d) Test discontinued at this time.

TABLE V Rupture, Total Deformation and Creep Data at 700~, 900~, 1100~ and 1200~F for 1.25 Cr-Mo-Si-V ("17-22A"S) Steel Aim Structure TempBHN erature (~F) Stre s s R uptur e Time (psi) (hours) Lower Pearlite 40% fine pearlite + 60% ferrite Middle Bainite 100% fine acicular bainite Upper Pearlite 45% medium pearlite + 55% ferrite Middle Pearlite 40% medium fine pearlite + 60% ferrite Lower Pearlite 40% fine pearlite + 60% ferrite Middle Bainite 100% fine acicular bainite Middle Bainite 100% fine acicular bainite Normalized 15% martensite + 85% coarse bainite 263 309 196 266 266 307 310 309 700 700 900 900 900 900 1100 1100 115,000 115,000 70,000 70,000 70,000 70,000 19,000 41,000 g 1827(d) 112 1484 1205(d) 1648(d) 815(f) 111.5 Elong - ation (% in 2 ") 19(c) 29(c) 13(c) 4(c) 2.5 Reduction of Area (%) 61 60 25 Deformation on Loading (in. /in.) 0. 0061 0.00570 0. 00406 0. 00323 0. 0010 Time to Reach Specified Total Deformations 0. 1% 0.2% 0.5% 1.0% a a a a a a a a 2 a a 65 a 30 222 45 24 53 2500(b) 575 Minimum Creep Rate (%/hour) 0.00029 0.00223 0.OOZZ00223 0. 00014 0.0015 3 3. 1 Upper Pearlite 237 1200 7,500 910(h) 0. 00030 40 182 590 0. 00066 45% medium pearlite + 55%. ferrite Lower Pearlite 293 1200 7,500 349 17 (e) 0. 00040 8 20 67 120 0.00656 40% fine pearlite + 60% ferrite (a) Specimen reached this deformation on loading. (b) Extrapolated value. (c) 0.250-inch diameter specimen, elongation % in 1-inch. (d) Test discontinued at this time. (e) Very badly scaled. (f) Broke in shoulder. (g) Broke on loading. (h) Test in progress.

TABLE VI Rupture, Total Deformation and Creep Data at 700~, 900~, 1100~ and 1200~F for 3 Cr-Mo-W-V (H-40) Steel Temp- Stress Rupture Elong- Reduction Deformation Time to Reach Specified Total Deformations Minimum BHN erature Time ation of Area on Loading Creep Rate (~F) (psi) (hours) (% in 2") (%() in. /in. ) 0.1% 0.2% 1.% (%/hour) - 700 90,000 1292(d) - -- 0.00424 a a 13 1770(b) 0.00011 Aim Structure Normalized 70% bainite + 30% martensite Oil Quenched 290 700 90,000 1514(d) -- - 0.00410 a a 16 1900(b) 0.00016 98% martensite + 2% ferrite Pearlite 193 700 90,000 24 22.0(c) 61.0 -- fine carbide precipitate Bainite 293 700 90,000 1170(d) -- - 0.00329 a a 1040 >2000(b) 0.00005 60% martaurite + 40% bainite and acicular ferrite Normalized - 900 65,000 1052 18. 0(c) 36.0 0.00316 a a 10 85 0.00418 70% bainitd f 30% martensite Oil Quenched 290 900 65,000 917 31. 0(c) 68.0 0.00360 a a 1 50 0.00485 98% martensite + 2% ferrite Pearlite 198 900 65,000 3.3 22.0(c) 68.0 fine carbide precipitate Bainite 309 900 65,000 1193(d) -- - 0. 00330 a a 20 296 0. 00061 60% martensite + 40% bainite and acicular ferrite Normalized 316 1100 31,000 720(e) -- 0.00146 a 7 274 677 0.00105 70% bainite + 30% martensite Oil Quenched 321 1100 30,000 865 20.0 26.0 0.00150 a 2 94 279 0.00237 98% martensite + 2% ferrite Pearlite 190 1100 30,000 23 49.0 82.0 fine carbide precipitate Bainite 313 1100 35,000 405 12,0(c) 33.0 0.00140 a VWO.2 13 110 0.00585 60% martensite + 40% bainite and acicular ferrite Normalized 310 1100 40,000 193 5 13.6 70% bainite + 30% martensite Normalized -- 1200 25,000 100 17 45 70% bainite + 30% martensite Oil Quenched - 1200 25,000 62 45 74 98% martensite + 2% ferrite Pearlite 200 1200 25,000 142 25 58 Fine carbide precipitate Bainite 293 1200 25,000 86 27(c) 52 60% martensite + 40% bainite and acicular ferrite (a) Specimen reached this deformation on.loading. (b) Extrapolated value. (c) 0. 250-inch diameter specimen, elongation % in 1-inch. (d) Test discontinued at this time. (e) Broke in threads.

X100D X1000D Figure 1. - Microstructure of Normalized 4340 Steel (Air Cooled after 1 hour at 17500F). X100D X1 000D Figure 2. - Microstructure of Oil-Quenched 4340 Steel (Oil Quenched after 1 hour at 1750~F). X100D X1000D Figure 3. - Microstructure of "Upper Pearlite" Obtained in 4340 Steel by Isothermal Transformation at 1240~F for 10 hours after Austenitizing for 1 hour at 1750~F.

X100D X1000D Figure 4. - Microstructure of "Middle Pearlite" Obtained in 4340 Steel by Isothermal Transformation at 1150~F for 14 hours after Austenitizing for 1 hour at 1750~F. X100D XO000D Figure 5. - Microstructure of "Lower Pearlite" Obtained in 4340 Steel by Isothermal Transformation at 1050~F for 111 hours after Austenitizing 1 hour at 1750~F.. X100D X1000D Figure 6. - Microstructure of "Upper Bainite" Obtained in 4340 Steel by Isothermal Transformation at 850~F for 28 hours after Austenitizing for 1 hour at 1750~F.

Figure 7. - X100D X1000D Microstructure of "Middle Bainite" Obtained in 4340 Steel by Isothermal Transformation at 750~F for 24 hours after Austenitizing for 1 hour at 1750~F. X100D X1000D Figure 8. - Microstructure of "Lower Bainite" Obtained in 4340 Steel by Isothermal Transformation at 650~F for 1-1/2 hours after Austenitizing for 1 hour at 1750~F.

X100D XIOOOD Figure 9. - Microstructure of Normalized "17-22A"S Steel (Austenitized at 1750~F for 1 hour and Air Cooled). '4;'.:. - ~., t. 1~~., $'~.',~;. X100D X1000D Figure 10. - Microstructure of Oil-Quenched "17-22A"S Steel (Oil Quenched after 1 hour at 17500F). Figure 11. - X100D X1000D Microstructure of "Upper Pearlite" Obtained in "17-22A"S Steel by Isothermal Transformation at 1300~F for 1-1/2 hours after Austenitization for 1 hour at 1750~F.

X100D X 1 OOO Figure 12. - Microstructure of "Middle Pearlite" Obtained in "17-22A"S Steel by Isothermal Transformation at 12250F for 1-1/2 hours after Austenitization for 1 hour at 1750'F. A..77:3~T;~QP ~ ~ '~ ',.3 'i ~.;',1r! f X100D X 1000D Microstructure of "Lower Pearlite"l Obtained in "117-ZZA"S Steel by Isothermal Transformation at 1150'F for 10 hours after Austenitization for 1 hour at 1750 F. Figure 13. - X100D XIOOOD Figure 14. - Microstructure of "Upper Bainite" Obtained in "17-22A"S Steel by Isothermal Transformation at 900'F for 2 hours after Austenitization for I hour at 1750'F.

XIOOD X1I000D Figure 15. -Microstructure of "Middle Bainite" Obtained in "17-ZZA"S Steel by Isothermal Transformation at 800'F for 1/2 hour after Austenitization for 1 hour at 1750'F. XC~ X100D X 1000D Figure 16. -Microstructure of "Lower Bainite" Obtained in "117-22A"S Steel by Isothermal Transformation at 700'F for 1/ 12 hour after Austenitization for 1 hour at 1750'F.

X100D X1000D Figure 17. - Microstructure of Normalized H-40 Steel (Austenitized 1 hour at 1950~F and Air Cooled).,.L.,- m-..,0 D. 1,. (CI Figure 18. Microstructure of Oil-Quenched H-40 Steel (Austenitized 1 hour at 1950~F and Oil Quenched). -....'... ~ ' ~.,..,,~,,.::-~.-.,~,~... <,~,~ ~.. ~..: ~. z~...., ~)'~ r t ~.'k-'s ' ~ '";~.... ~ ' " ~',""~ ~i~: -/..:~K..:''~~'', " — ~~-.'.,, '-'- ". X 100D X 1000 Figr18 hour at 150~F and i ~unhe)

X100D X000D Figure 19. - Microstructure of "Pearlite" Obtained in H-40 Steel by Isothermal Transformation at 1300~F for 24 hours after Austenitization for 1 hour at 1950~F.... X100D X1000D Figure 20. - Microstructure of "Bainite" Obtained in H-40 Steel by Isothermal Transformation at 7500F for 10 hours after Austenitization for 1 hour at 19500F.

TABLE I Type Structures, Heat Treatments and Actual Structures for 4340 Steel (All 4340 bar stock austenitized at 1750~F for 1 hour.) Aim Structure Transformation Conditions Temp- ~F Time-hrs 1240 10 Approximate Structure Obtained Upper Pearlite Middle Pearlite Lower Pearlite Upper Bainite Middle Bainite Lower Bainite Normalized Oil Quenched 1150 1050 850 750 14 111 28 24 80% medium pearlite + 20% ferrite 95% fine pearlite and fine carbide-ferrite aggregate + 5% ferrite 99% very fine carbideferrite aggregate + 1% ferrite 70% upper bainite + 30% martensite 100% medium acicular bainite 100% lower bainite 35% martensite + 65% bainite s 100% martensite BHN 212/221 197/223 255/275 319/327 293/313 430 385 585 Tempering Temp-~ F Time-hrs None None None None BHN 212/221 197/233 255/275 319/327 650 1-1/2 Air cooled from 1750 Oil Quenched from 1750 None 1100 1100 1100 293/313 1-1/4 1 10 277/301 300/311 304/309

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