THE U N I V E R S I T Y OF M I C H I G A N COLLEGE OF ENGINEERING Department of Naval Architecture and Marine Engineering Final Report MODEL TESTS OF PROJECT MOHOLE DRILLING PLATFORM F. C. Michelsen N. Rabe ORA Project 06333 under contract with: BROWN AND ROOT, INC. HOUSTON, TEXAS administered through: OFFICE OF RESEARCH ADMINISTRATION ANN ARBOR August 1964

TABLE OF CONTENTS Page LIST OF FIGURES v 1. INTRODUCTION 1 2. MODELS AND INSTRUMENTATION 4 2.1 Drilling Platform and Main Propellers 6 2.2 Positioning Unit 8 3. DATA AND FULL SCALE PERFORMANCE PREDICTIONS 14 3.1 Towing Tests (EHP Tests) 16 3.2 Open Water Tests of Main Propellers 19 3.3 Self-Propulsion Tests 19 3.4 Steering Propulsion Unit 20 11i

LIST OF FIGURES Pages Figures 3.1.1 - 3.1023 EHP Tests 23-45 Figures 3.2.1 - 3e2,4 Main Propulsion Open Water Tests 46-49 Figures 3.3.1 - 3.3.49 Self-Propulsion Tests 50-98 Figures 3.4.1 - 3.4.15 Positioning Unit 99-113

1. INTRODUCTION This report presents the results of resistance and self-propulsion tests performed with a model of the Mohole Drilling Platform. The general arrangement of the prototype is shown in Figure 1.1 (Brown and Root Drawing 1-T-10002). Size of model was selected on the basis of propeller diameter. To avoid significant scale effect in propeller performance, the propeller diameter was made equal to 7 in. (16'-0" full size) which led to a model scale ratio of approxixmately 27.5. Under these conditions the size of the model was such that a blockage effect existed when towing the model in the model basin. On the basis of past experience with conventional ships this blockage effect was estimated to increase the resistance by about 3%. In addition to testing the platform, the performance of the steering propulsion unit was also investigated as part of this test program. The arrangement of the steering unit prototype is shown in Figure 1.2. The model was built to a scale ratio of 7.5 which made the propeller diameter 9.2 in. (5'-9" full size). In outline the total test program conducted is as follows: 1.1 Measurements of steady state resistance, side force yaw, trim and heel moments under the following conditions: 1.1.1 28' draft (transit condition) at headings of 00, 100, 200, 900, and 180~, and at speeds up to 12 knots for headings of 0~, 10o, and 200, up to 4 knots for 900 heading and 8 knots for 1800~ 1. s2 70' draft (drilling condition) at headings of 00, 100, 200, 45~, 90~, 135~, and 1800, and at speeds up to 8 knots for headings 0~ and 180~, 6.5 knots for 100,5.0 knots for 20~, and 4.0 knots for headings for 45~, 900, and 1355. 1.2 Self-propulsion tests of the platform, in which propeller torque, thrust, and rpm of both propellers were measured in addition to quantities listed under 1.1, under the following conditions: 1.2'.1 28' draft (transit condition) at headings of 00, 20. and 180~, and at speeds up to 12 knots for Oc, 9 knots for 200 and 1800 with propellers operating astern and 6 knots for 180~ with propellers operating ahead. Propellers run in incremrental steps up to maximum power of 8,000 hp. 1.2.2 70' draft (drilling corndition) at headings of 0~, 20~, 405~, 1355, 160~, and 180~, and at speeds up to 6.3 knots for 00 and 180~, 1

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GUIDE RAILS LIFTING CABLES LIFTIN CALS TPOWER & CONTROL CABLE 9'-0"I.D. TUBE - GUIDE ROLLERS, i WATER TIGHT CAPSULE PROPULSION 1 -_T -ACCESS HATCH PROPULSION MOTOR RCT IO l 1 i b SMOTOR FOUNDATION UPPER SEAL GLAND MOTOR DECKROTATION "'i,';-_ ~-S'.-FIRST STAGE REDUCTION GEARS DRIVE WORM --— _ —. I GEAR HOUSING THRUST BFARING - SEATING PAD LOWER SEALING - GLAND —. GL-A 07- ==BASE LINE__ _ v o.., c0wCOVER PLATE SHAFT CENTERLINE f! PROPELLER & NOZZLE SUPPORT STRUT /.-, I I. —.: -.. —-—. —-- SECOND STAGE REDUCTION,.~ GEAR POD NOZZLE SUPPORT STRUCTURE CONCEPTUAL SKETCH OF RIGHT ANGLE DRIVE UNIT DETAIL-A (NOSCALE Fig. 1.2

4.75 knots for 20~ and 160~, and 3.75 knots for 45~ and 135~. Incremental power loading was done in a manner similar to the procedure used under 1.2.1. At angles above 900 the model was also tested with propellers operating astern. 1.2.3 "Bollard pull" in drilling and transit conditions at speeds of about one knot and over the range of angles covered under 1.2.1 and 1.2.2. Propeller was run at near maximum power. 1.3 Open water tests of steering propulsion units at headings of 0~, 300, 60~, and 850. The unit was tested over a complete speed range from bollard to free wheeling (no thrust) at constant rate of rotation. Both 600 and 800 rpm were used and it was verified that no noticeable Reynolds number effect existed. The steering propulsion unit was also tested under bollard conditions when placed under a model simulating the platform hull. The axis of this model was always transverse to the towing tank whereas the steering unit was tested at all heading angles listed above. Furthermore, performance over a small range of advance coefficients was investigated. 1.4 Open water tests were performed with both main propulsion propellers. The propellers were tested operating in a nozzle of the same dimensions as the nozzles designed for the drilling platform except that the angle of attack of the nozzle foil section was reduced to make it equal to the value given by Van Manen for unobstructed inflow conditions. The force on the nozzle was not measured. The nozzles were considered an integral part of the drilling platform and were, therefore, built as fixed appendages. Both propellers were tested at straight inflow conditions and one propeller (left hand) was tested at an inflow angle to the propeller axis of approximately 10~ and 20~. It was found that within this range of angles the propeller characteristics were not significantly altered. Free-wheeling propeller tests were also run to determine the velocity increase at the propeller disc produced by the nozzle, and also the change in average velocity due to a non-zero angle of inflow. Free wheeling propeller tests were also run with the propellers in their normal running position which allowed an independent evaluation of advance coefficients to be made, different from that normally made by comparison of propeller performance behind the hull and the open water propeller characteristics. 1.5 Deceleration tests were made at drilling platform headings of 00, 900, and 1800 at 70 ft draft. It was initially intended to conduct acceleration tests. A careful consideration of all factors such as the number of readings, noise level of records and the fact that the towing carriage does not provide for positive acceleration control lead to the conclusion that the desired information could most easily be obtained by releasing the model from the carriage when moving at constant speed and subsequently the speed of the towing carriage be continuously adjusted to that of the deceler14

ating free moving drilling platform. This scheme was then used during 8 to 15 runs at each of the headings mentioned above. The large number of runs was necessary to develop a sufficiently coordinated testing pattern by the testing personnel.

2. MODELS AND INSTRUMENTATION 2.1 DRILLING PLATFORM AND MAIN PROPELLERS The model was made almost entirely from aluminum. Cylinders were rolled from 1/8 in. aluminum plate. The vertical cylinders were made in such a way that their length could be adjusted to the draft of the model. This was necessary to allow the model to fit under the carriage during testing. The two longitudinal units each consisting of one longitudinal cylinder and three vertical cylinders were connected by three pairs of 4 in. aluminum channels, bolted together at the joints. The model is shown during testing in Figure 2.1.1. Figure 2.1.1 the aluminum cylinders with wood screws. Propeller dynamometers and drive motors were mounted on a foundation attached to the tail pieces. Thus, it was possible to readily remove the whole tail assembly including propeller drives for installation and alignment. Fins were made of aluminum plates 1/8 in. thick. The nozzles were turned on a lathe from a block of Plexiglass. The profile of the nozzles is shown in Figure 2.1.2. After some difficulties experienced in obtaining aluminum cast6

MAIN PROPULSION FOR MODEL TESTS NOZZLE 0.009 I~. NOZZLE SECTION OFFSETS x/1 x 100 A/o x 100 B x 100 C/_ x 100 O 23.43 18.33 5.10 2.5 23.89 13.99 9.90 5.0 23-35 1.0O6 12.29 7-5 22.81 8.87 13.94 10.0 22.26 7.08 15. 18 15.0 21.17 4.48 16.69 20.0 20.09 2.64 17.45 25.0 19.01 1.43 17.58 30.0 17.92 o.65 17.27 40.0 15-75 0.08 15.67 50.0 13.58 0 13.58 6o.0o 1. 41 0 1.41 70.0 9.24 0.12 9.32 80.0 7.07 0.53 6.54 90.0 4.90 1.10 3.80 95.0 3.81 1.45 2.36 100.0 2.73 1.78 0.95 NOZZLE SECTION IS MODIFICATION OF VAN MANEN NO. 18 Sketch RT-117-01 27 December 1963 PROPELLER 4 Bladed Kaplan Type ( K4-55) Diameter 16'- 0" Pitch 13' -11" Figure 2.1.2 7

ings for the main propellers, it was decided to manufacture them entirely by hand from a block of magnesium. This proved in general to be a success, although a check of finished propellers revealed that the left hand propeller was about one half percent overpitched and the right hand propeller about 5-1/2% overpitched. The difference in pitch is thought to be mostly due to release of built-in stresses. The performance characteristics of the two propellers are completely compatible, however, in that one curve can be calculated with sufficient accuracy from the other simply by taking the pitch variations into account. All dynamometers for measurement of the forces and moments acting on the platform were attached to a 4 in. x 4 in. wooden beam which was always oriented along the carriage centerline. The drilling platform was attached to this wooden beam, and was rotated around a bolt located at the intersection of the longitudinal centerline of the platform and the transverse centerline of the middle vertical cylinders when tested at non-zero heading angles. As a result, test data refers initially to the carriage coordinates. These correspond to what may be considered the flow coordinates and the force components measured in the horizontal plane are therefore designated Drag and Lift. Decomposed to the platform coordinates the forces are referred to as Resistance and Side Force. Figure 3.0.1 illustrates these coordinates. Yaw moment is taken with respect to the bolt location referred to above. Other moments are those of trim and heel. During deep draft tests it is inevitable to introduce trim and heel moments because the tow bar and side force attachments are located about 15 in. above the water surface on the model. A system of loading and unloading weights at specified points was therefore desired so that the model would remain essentially horizontal during testing. The magnitude of the corrective moments when applied were recorded. In no cases were they found to be required under transit conditions and neither did the self-propelled test ever cause any significant trim and heel conditions, except under drilling conditions when propelled opposite to direction of motion. Even under these severe conditions the trim and heel moments were not excessive. It is fairly safe to conclude that heel and trim due to hydrodynamic drag and lift together with propeller thrust should not be of much concern in the case of the full size platform. 2.2 POSITIONING UNIT The overall model design is shown in Figure 2.2.1. Because this figure

includes both dynamometer parts in addition to the steering unit itself, a Figure 2.2.1 few words of description of the various parts are in order. The steering unit tests were designed to measure side forces at non-zero heading angles as well as the force developed in the direction of motion, all as a function of torque, propeller rpm, and carriage speed. To accomplish this, a platform was suspended by four leaf springs, one at each corner, from two transverse channels fastened to a floating beam dynamometer which was already available. The leaf springs allowed a fairly free lateral motion relative to the longitudinal dynamometer beam. Load cells introduced to restrain this motion would therefore measure almost the entire lateral force, thus providing good resolution of data. The entire system is linear and the complete dynamometer was calibrated by applying known side forces statically to the platform. Because two load cells were used, one at each end of the platform. it was hoped that turning moments could be evaluated from the record. In this respect we were disappointed, however, when final calibration revealed that the separation of forces between the two load cells depended upon the moment of forces around a longitudinal axis.

The drive motor and torque transducer were located on the platform. The propeller was driven through two pairs of bevel gears (1:1 ratio). Since the propeller was to be tested at various heading angles, it was found necessary to make the vertical strut in two parts. The upper part was fixed, and all the data were corrected to compensate for the fixed portion of the strut. The steering propulsion unit model is shown in greater detail in Figure 2.2.2. Figure 2.2.2 The diameter of the aluminum propeller was 9.2 in. and the Plexiglass nozzle was made in accordance with dimensions given in Figure 2.2.3 allowing a 1/32-in. clearance between propeller blades and nozzle. The principal prototype propeller dimensions are also given in Figure 2.2.3. The propeller axis was located at a depth of about 17 in. below the free surface during testing. This depth was increased during the testing of the steering propulsion unit under the semi-cylindrical shell which simulated the drilling platform hull. This semi-cylindrical shell consisted of a masonite sheet wrapped around a wooden frame made to dimensions given in Figure 2.2.4. The shell was attached directly to the carriage. No contact existed between steering propeller unit and shell. It has already been mentioned that dynamometer forces were calibrated by applying forces directly to the dynamometer. To this should be added that 10

STFERING UNIT PROPULSION FOR MODEL TESTS NOZZLE _.0.86 IN. C 0O. 31 IN. 11.7' 34 5 IN. KORT NOZZLE FOR POSITIONING UNITS MOHOLE DRILLING PLATFORM NOZZLE SECTION OFFSETS x in: A in B in C in 0 7.90 6.14 1.76.86 8.07 4.65 3.42 1.72 7/89 3. 5 4.24 2..59 7.71 2.90 4.81 3.45 7.53 2.29 5.24 5.18 7.17 1.40 5.77 6.9o 6.82.78 6.o4 8.62 6.46.37 6.og 10. 35 6.o.17 5.93 13.80 5.39 0 5.39 17.25 4.67 0 4.67 20.70 3.96 0 3-96 24.15 3.25.12 3.13 27.60 2.53.28 2.25 31.05 1.82.52 1.30 32.78 1.46.65.81 34.50 1.10.81.29 NOZZLE SECTION IS MODIFICATION OF VAN MANEN NO. 18 Sketch RT-117-04 20 March 1964 PROPELLER 4 Bladed Kaplan Type (K4-55) Diameter 5'-9" Pitch 5' -0" Figure. 2.2.3 11

SIDE VIEW C ~ ~~~~~~~ I,, 4'-8POSITIONING UNIT STRUT8 8 -0" WL 2'-7 " 2'-42~" 4/ 4 i~.. Fig._

the torque dynamometer was calibrated dynamically against a calibration generator. Since this generator was attached directly to the propeller shaft during calibration, it was possible also to evaluate the friction loss in the bevel gear drive as a function of load and rpm. 13

3. DATA AND FULL SCALE PERFORMANCE PREDICTIONS Before referring to the detailed test results it may be advantageous to list here definitions of all symbols used in the figures. These are as follows: Towing Tests D Component of hydrodynamic force in pounds on the platform parallel to the direction of motion. Positive D is in direction opposite to Vk vector. L Component of hydrodynamic force in pounds on the platform perpendicular to the direction of motion.!L is positive if it is at an angle of + 900 to Vk. M Yawing moment in foot-pounds acting on the platform measured about the intersection of the fore and aft centerline and the line connecting the centers of the middle vertical cylinders. Positive moments are counter-clockwise. R Component of hydrodynamic force in pounds on the platform parallel to the longitudinal centerline. Positive R acts opposite to the direction of the component of the Vk vector parallel to R. S Component of the hydrodynamic force in pounds acting on the platform perpendicular to the longitudinal centerline. Positive S acts at an angle of + 90o off the bow. Vk Speed of platform in knots. G Angle of model to flow in degrees. Positive e is measured clockwise. Open Water Tests of Main Propulsion Propellers d Diameter of propeller in feet. n Revolutions per second. 14

T Propeller thrust in pounds. Q Propeller torque in pounds. Va Velocity of advance in feet per second (carriage coordinates). p Density of water in slugs per cubic foot. V Ja Advance coefficient, nd T Kt Thrust coefficient, pn2 d4 Kq Torque coefficient, pn2 d5 Kt Ja Propeller efficiency, K 2 Vm Velocity of model in feet per second (carriage coordinates). Self-Propulsion Tests DpLpMrRp,Sp Hydrodynamic forces on the platform with the propellers running. They are defined exactly the same as the un-subscripted forces. Tp Total propeller thrust in pounds along propeller axis. t Propeller-hull interaction force in pounds. Positive t in the same direction as Tp. SHP Total shaft horsepower. Other symbols used in this section have been previously defined. 15

Positioning Unit T Force component exerted by unit parallel to Va vector. Positive T is in same direction as Va. Fs Force component exerted by unit perpendicular to Va vector. Positive Fs acts at an angle of + 900 to Va. T Kt Thrust coefficient, pn2 d4 Fs Ks Side force coefficient, pn2 d4 Dn Drag of the nozzle and strut in pounds with the propeller freewheeling. Positive Dn is in direction opposite to Va vector. Ln Lift of the nozzle and strut in pounds with the propeller freewheeling. Positive Ln is in direction + 900 from Va vector. Other symbols used in this section have been defined previously. Figure 3.0.1 illustrates clearly the definitions of the forces acting on the platform. Although all tests are parts of the same overall program it soon became convenient to refer to individual sections almost as separate programs by themselves. This breakdown has been carried over into this report as follows. 3.1 TOWING TESTS (EHP TESTS) It was stated in the introduction that size of towing tank (maximum width of 22 ft) imposed an upper limit on model size. This was much in evidence when testing at angles of around 45~ yaw. Initially, it was thought that at these large angles the blockage would be quite significant. A careful look at the streamlines around the ends when testing under transit conditions revealed that the flow around the longitudinal cylindrical hulls had become, to a large extent, two dimensional, however, and the blockage effect was not judged to have been greatly changed due to large yaw angles. A more serious question may be that concerned with Reynolds number effects. The strange behavior of circular cylinders as a function of Reynolds number is 16

FIGURE 3.0.1 Vk DEFINITION OF COORDINATE SYSTEMS +M 1! +D Vk FLOW COORDINATES SHP +M/ I CORDNAE SHIP COORDINATES j

well known as is the conclusion reached from it that t is imperative to make the boundary layer flow turbulent somre distanee ahead of mtaximlum beam. To accomplish this, wide longitudinal strips of coarse sandpaper were glued to all. cylinders every 450 of circumference. We are quite confident that these strips did perform satisfactorily. Previous tests with two models of an oil drilling platform rade to different scale ratios tindicate that the IaminarturbuLent transition takes place at a model size considerably smaller than that of the Mohole drilling platform. It is also of intaerest to note from Figure 3.l121 that extrapolation of data by the usual ship method using the ATT friction line gives results only a little below the simple X3 extrapolation. The nature of the flow is probably such that a 23 extrapolation (hydrodynamic forces proportional to the square of the velocity) is a better approximation than the A'C method. In essence it implies that the resistance is independent of the Reynolds number. In this report the ~3 extrapolation is used throughout. A 35 allowance has been made for the difference in density of salt and fresh water. A different flow separation problem of interest is that occurring at the transition between the longitudinal cylinders and the stern sections. This problem was studied to some extent both in the transit and drilling conditions. The separation under transit conditions and 0 ya is shown in 1Figue *.0 to be severe. ~~~~~-..........;ig u r e.. indicates the wake region behind the points of separat'on. A floating par18 Ttz~~ pic~~t~~ure was t~~~dfcen w~~th a~~~ufninwn ps~~~wdclp- on Lhe surface and ~~~~~~he darlt; arcrx77i $ndicra~~~~~ces tT~~~e wake r~~~~~gion'ftrthind t~~~~~~~he poin-t~~~~~a o-f separal~~~~~~on. A fl~~~~~oa-t~~~........ t~~iclc in ~f~his region wou~~d ssm~-t~imes fO~xlow ~~ht~t fn~del, -t~fit~~ wfnol~.................

The situation does not appear to be quite that serious under drilling conditions. Separation could here best be observed by injecting aluminum powder mixed with alcohol through a tube into the flow. Separation seemed to occur half way aft on the stern section, but with the propeller working the flow appeared to be stabilized. Figures 3.i.1 through 3.1.10 show the performance of the platform during transit conditions (28 ft draft). Figures 3.1.11 through 3.1.20 cover the same for drilling conditions (70 ft draft). Figures 2.1.22 and 2.1.23 give the results of the deceleration tests (70 ft draft). These results are a little startling. A priori it was expected that the deceleration would-be smaller than that obtained from Newton's law using the steady state drag as a force. The reason for this was based on the idea of the hydrodynamic mass. Results show, however, that at 00 heading and at speeds close to release speeds the deceleration measured is higher than expected. The platform was apparently adding to the fluid rather than recovering from it kinetic energy as it is slowing down. The behavior is as expected at the lower speeds and also for 90~ heading. This phenomena may need further investigation. 3.2 OPEN WATER TESTS OF MAIN PROPELLERS Propeller tests were made with the propeller boat in the usual manner except that a Plexiglass nozzle was attached to the propeller boat. Only forces acting on the propellers were measured. The characteristics curves of the right hand propeller are shown in Figure 3.2.1. This propeller, being about 5-1/2% overpitched was tested only in axial flow. Figure 3.2.2 shows the same curves for the left handed propeller in addition to those obtained for 100 and 200 angle of flow relative to propeller axis. It is interesting to note that the propeller performance is for all practical purposes not influenced by inflow angles up to at least 200, which was the maximum angle that could be investigated without modification of existing testing facilities. Free wheeling test results given in Figures 3.2.3 and 3.2.4 reveal that the nozzle serves as a very good flow deflector so that the average velocity of the flow at the propeller disc is fairly constant with respect to angle of inflow over the range of angles considered. 3.3 SELF-PROPULSION TESTS The objective here was to study the change of dynamometer forces as a function of shaft horsepower output of the main propellers. The same quantities were therefore measured as under Section 3.1 and plotted versus SHP, with angle of heading as a parameter. SHP was obtained directly from the propeller dynamometers installed in the model. The dynamometer in the starboard 19

unit measured torque, thrust and rpm whereas a rented dynamometer in the port unit only measured torque and rpm. The speeds of rotation of the two propellers were adjusted to correct for the difference in pitch. As expected it was found that the propeller nozzles were developing a significant thrust force. Unfortunately, we were not instrumented to measure this force by itself, but it was possible to calculate by the use of the propeller curves a thrust interaction force which would include the nozzle thrust and the force normally referred to as thrust deduction. This interaction thrust can be either positive or negative and several non-diriensional ratios can be formed by dividing it with other forces acting on the platform. Because of this multiplicity of choice it was decided to plot only the measured dimensional force. The extrapolation of the SHP data to the ship scale was carried out in the standard manner with one exception. Normally, in SHP tests, a small correction is made in extrapolation to account for Reynolds number effects. As previously stated, Reynolds number effects were found to be negligible with this model. Thus thrust is extrapolated according to in the same way as in drag. Torque is proportional to. and rpm to % ~5. Since SHP = constant x torque x rpm, shaft horsepower is proportional to %3*5.* Self-propulsion tests were run at several headings under both transit and drilling conditions. Figures 3.3.1 through 3.3.13 cover the transit condition, whereas Figures 3.3.14 through 3.3.48 refer to tests performed at the drilling operation draft of 70 ft. Figure 3.3.49 shows the platformperformance at bollard pull. 3.4 STEERING PROPULSION UNIT The steering propulsion unit has already been described in some detail under Section 2.2. Nondimensional plots of propeller characteristics are shown in Figures 3.4.1 through 3.4.15 covering tests with and without simulated hull model in place. In reducing the test data it was at first believed necessary to add to the thrust force in the flow direction the drag of the strut and the nozzle. Because it was thought that this drag, being primarily due to the boundary layer and eddies, would not behave as a potential flow. However, it was found that non-dimensional coefficients calculated from total measured forces obtained from runs at constant values of the advance coefficient but at two different rpm's (600 and 800) would plot on the same curves. It was, therefore, decided that it would be most suitable to use total measured forces. The force acting on the unit without the propeller in place is given in Figure 3.4.15. *Principles of Naval Architecture, Rossell and Chapman, Vol. II, S.N.A.M.E., Chapter 3. 20

All variables are referred to the flow coordinates, i.e., the thrust coefficient is evaluated from the force measured in the direction of inflow (direction of motion in the stationary fluid). Performance characteristics can easily be transferred, however, to the coordinate system fixed in the positioning unit, or any other coordinate system in which magnitude of force components are needed, by the use of Figure 3.4.9. A line in this figure extending from origin to a point on a contour of constant G represents the total force coefficient at a particular value of the advance coefficient. This force coefficient can then be decomposed into any two directions. In Figure 3.4.9 the vertical axis represents the thrust coefficient in the direction of flow and the horizontal axis represents the side-force coefficient. Contours of constant values of advance and torque coefficients have been added to the figure so that in reality it represents a complete performance chart of the steering propulsion unit. 21

ACKNOWLEDGMENTS A. test program as unique as the one described in this report will usually demand a great deal more from those taking part in it than will a more routine job. The final results depend, therefore, to a large extent upon how test personnel respond to this demand. Without exception it has been the gratifying experience of the authors to witness efforts put forth by all concerned with the Mohole Project far beyond what would normally be expected. A. majority of our staff members have at some time or another worked on this program and to mention everyone by name is perhaps not necessary. However, the authors wish to give special recognition to Mr. Phil Schnell who supervised the construction of the aluminum platform model and many more of the model details. Also Mr. Corning Townsend deserves to be mentioned for his effort in designing and building the steering propulsion unit. In addition he was responsible for much of the tesing of that unit. Last but not least, Mr. John Gebhardt and Mr. Bruce Nelson have contributed a great deal towards the completion of the testing program. Theirs has been the task of running many of the tests and the reduction of most of the data. 22

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RESULTS OF BOLLARD PULL TESTS Vk = 1.0 knots 28' Draft Angle; 0 RPM SHPxlO-3 Dpx1O 5 Lx105 Rpx1O5 SpX105 Mx10-6 O 131.35 16.874 -5.095 0 -5.095 o 20 127.19 16. 616 ---- ---- ---- ---- ---- 45 131.00 16.462 -3.348 3.868 -5. 103.368 1. 716 135 127.38 16.696 4.305 2.912 2.460.468 12.582 160 127.00 15.926 5.075 -.562 4.577 2.263 - 2.574 180 129.75 16.684 5.407 0 5.407 0 0 70' Draft 0 RPM -3 - - 5 -5 -ss5 -6 Angle; ~ RPM SHPxlO DpxlO 5 pxlO 5 RpxlO MpxlO O 132.72 18.116 -5.165 0 -5. 165 0 20 132.72 18.201 -4.640 1.851 -4.991.153 3.717 45 132.72 18.901 -2.912 4.388 -5.162 1.044 5.433 135 132.72 18.620 4:534 3.182 5.456.956 7.721 135 Rev. 132.72 15.623 -.312 -2.724 -2.147 1.706 23.735 160 132.72 18.543 5.511 ~ 957 5.506.986 7.435 160 Rev. 132.72 14.676 -1.456 -1.270 -1.788.655 8.865 180 128.26 16.414 5.345 o 5.345 0 0 180 Rev. 127.57 12.523 -1.58t -1.581 o o0 Fig. 3.3.49 98

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03 Kq.02 01 0 0.1 0.2 O.3 0.1 4' J. 0,5 0.6.047 0.8 0.9 101:;;:;:;:::.:;::;: X i:::;:.........

0. 03 K q 0.02 0 0 l0: 200 30~ 4L0 5Q0 600 78 80: 900 102

K 0.4 0.2 0.1 0 6 0 0.1 0.2 0.3 0.4 J 0.5 0.6 0.7 0.8 0.9 a 103

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0.6 0.4 0.3 0.2 0.1 -0.1 0 0.1 0.2 0.3 0-14 Ja0.5 0.6 0.7 0.; 0,9 a

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ADDENDUM STEERING UNIT PROPELLER.5R Pitch = 7.850'r.7R = 7.856'r.9R = 7.905'r For a P =.875 and DIA. = 9.2'1 the required pitch is PR =.875 x 9.2 = 8.05'r Using an average actual pitch of 7.87'r the propeller is underpitched by 8.'05 - 1) 100 = 2.3% 7.87 To convert the given torque coefficient to the correct geometry prope ler it is necessary to multiply values given in the graph by (1.023)2 = 1.0465. However, the new KQ should be plotted at an advance coefficient which is 2.3% greater than the value read from the figures. A much easier procedure is to simply calculate the torque and thrust from the graphs and apply these to the correct propeller rotating at a 2.3% slower speed than the model propeller. 114

-co~: \- t co_,