Text

Partial Response to FOIA Request for Documents Re Pressure Suppression.Forwards App a & B Documents.Documents Also Available in Pdr.App B,Document 3 Available from Natl Technical Info Svc
	ML20207T985
Person / Time
Site:	Humboldt Bay
Issue date:	03/20/1987
From:	Grimsley D; NRC OFFICE OF ADMINISTRATION (ADM)
To:	Thomas P; SIMPSON, THATCHER & BARTLETT
Shared Package
ML20207T986	List: ML20207T985; ML20207U023; ML20207U059;
References
	FOIA-87-40 NUDOCS 8703240473
	Download: ML20207T985 (4)
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{{#Wiki_filter:. _ _ _ _ _ _ _ _ _ _ _ _ _. _ _ _ .a ae:e,\\ i UNITED STATES + [ ' 3 v. c g NUCLEAR REGULATORY COMMISSION O(h 5-W A5HING TON, D. C. 20655 t / %...../ Peter C. Thomas, Esquire Simpson, Thacher & Bartlett W 20 W One Battery Park Plaza IN RESPONSE REFER New York, New York 10004 TO F01A-87-40

Dear Mr. Thomas:

This is in partial response to your letter dated January 16, 1987. in whichyourequested,pursuanttotheFreedomofInformationAct(FOIA), four categories of information concerning pressure suppression, which were clarified in the agreement reached in the meeting on January 16, 1987 regarding the scope of your request. This also confirms infomation relayed during that meeting and numerous subsequent telephone conversations between members of your law firm and my staff concerning this request. CATEGORY ONE in telephone conversations with Carol Ann Reed on January 27. February 3, and February 5,1987, you or Jack Menz were informed that the accession lists for Quad Cities, Cooper Brunswick, Shoreham, Limerick, Monticello, GESSAR, Grand Gulf, and Humboldt Bay (except pre docketed material)werealreadyavailableintheNRCPublicDocumentRoom(PDR). You agreed to review these lists and submit new F0!A requests for any documents you want reproduced. Enclosed are the accession lists for Zimmer and the pre-docketed material for Humboldt Bay. These lists are also being placed in the POR. In a telephone conversation on February 5 between Carol Ann Reed and Jack Menz, he was informed that the only item not reproduced concerning the Bodega Bay Central File's docket file in response to a previous FOIA request was a document entitled "The Battle of Bodega Bay." This document is a collection of newspaper articles concerning the opposition to the plant. Mr. Menz indicated that you did not want a copy of the document. In the meeting that took place in Bethesda on January 16, 1987, were informed that you should contact the Department of Energy (you00E)for several of the items you requested. You were also informed that information subject to your request could be located in POR folder F0!A 85-782 under the name of Morrow. e703240j73870320 MMA 7 40 PDR I

CATEGORY TWO In the January 16, 1987, meeting, we agreed to contact the current NRC employees and Historian to detemine if they have any documents i subject to your request. The document listed on the enclosed Appendix A has been located and is enclosed. This document is also being placed in the PDR. For your information, Mr. McCone's official files are located at DOE and his personal papers are located at the Dwight D. Eisenhower Library in Abilene, Kansas. This completes action on this category. CATEGORY FOUR The documents listed on the enclosed Appendix B have been located and I are enclosed except for document three. Document three is available for purchase from the National Technical Infomation Service in Springfield, Virginia. Documents one, two, and six were located by the NRC Library staff using DIALOG which is a commercial information retrieval system. Documents four and five were located in the NRC's Topical Reports file. Document seven, although not specifically requested, was located by the NRC Library staff using the various authors' names included on your list. I With the exception of document five, which contains General Electric proprietary information, the Appendix B documents are also being placed in the PDR. t l Since you agreed to pay the reproduction charges and any applicable search fees, you will be billed in accordance with the charges specified in 10 CFR 9.14(b) by the hRC's Division of Accounting and Finance upon the completion of this request. For your information, the reproduction charge for the enclosed documents is $109.10. If you have any questions, please telephone Carol Ann Reed on (301)492-4262. Sincerely, 1 .2._ _ s 7 j ()r.4onttleH.Grimsley, Director Division of Rules and Records l Office of Administration l

Enclosures:

As stated i I 1

e* Re: F0!A-87-40 APPENDIX A i 1. 3/31/60 Memo for the General Manager from J.A. McCone with typed l noteatbottom.(1page) i r i r b i f 1 i l 1 I. [ P r I ( c

Re: F0!A-87-40 APPENDIX B 1. 4/3/59 GEAP-3143 " Test Report for the Pressure Suppresion DevelopmentProgram"(Thisreportisalsolocatedinthe HumboldtBaydocketfile.) 2. 11/17/60 GEAP-3596 " Tests of a Full Scale 1/48 Segment of the Humboldt Bay Pressure Suppression Containment." 3. 3/61 HW-68609 "NPR Primary Loop-Emergency Dump Test:;."

4.

5/64 BAW-3198-2 " Closed Tank Vapor Suppression Test Program." 5. 5/70 NEDE-10182 " Additional Information Pressure Suppression Concept Test Data Report." 6. 7/70 NEDM-13036-1 " Pressure Suppression Pool Investigations Report #1." 7. 8/62 Article by C.P. Ashworth. 0.8. Barton and C.H. Robbins " Pressure Suppression" in Nuclear Engineering a British journal.

Paper copy not available

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NRC F@r41ES U. S. NUCUIAA C31EULATC2Y CCMMIS$10N PAGE 19-76) DOCUMENT RECORD 1 APPLICANT DOCKET NUMSER PACIFIC GAS & ELECTRIC COMPANY Humboldt Bay 50-133 DATE DESCRIPTION OF DOCUMENTS DOCKETED

*
DENOTES SENT TO NRC POR
* *
DENOTES SENT TO LOC AL POR PRE-DOCKETED CORRESPONDENCE Ltr 2-12-53 fm PGE confinning telecon and transmitting GE ltr dtd 2-12-58 re the preliminary evaluation of Eureka PG&E site....also enclosed maps, drawings........

Ltr 5-23-58 fm PG&E ref telecon confirming meeting of May 28 Ltr 3-31-59 to PGE in ref to their 3-23-59 ltr requesting Fonn AEC 2 and info for use in connection with applying for a-utilization facility construction pennit and an allocation of special nuclear material April 23, 1959 Ltr 4-20-59 fm PGE trans: GEAP-3143 " Test Report for the Pressure Suppression Development Program dtd 4-2-59 9 0 CONTINUED ON NEXT PAGE NMC FORM lit (9 79)

-. y- ;&s yw o~ 1 -A ~r roe uma er s=oumes==i.v GEAP--3143 SEN ER AL $ ELECTRIC oces o133,3 ATOMIC POWER EQUIPMENT DEPARTMENT TECHNICAL INFORMATION SERIES Tev6a Pant bO CD - ?(E T S d C 3 ( aurmes s euence e6AsetF15AvleN No.GEAP 3143 1 W. L. Flock Reactor Containment

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E. Janssen aan A. G. Steamer April 3,1959 TEST REPORT IOR THE PRESSURE SUPPRESSION DEVELOPMENT PROGRAM Pacific Gas and Electric Conpany sponsored a ^""'" development program for the pressure suppression system of reactor contairvnent. This program in:1uded a condensing test facility to investigate large scale steam injection equipment performance and a small scale transient test facility to obtain pressure response data for a coeplete system. The results of tests conducted with (cont'd below) ..:. cua... ..noooeistaca.,rioso av

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APED Library e av. ci.4.. The test results were highly successful with so c6ueio.. respect to verifying and extending the technology of the pressure suppression containment system. The condens-ing tests indicated that the steam injection equipment may be sinple and that condensation is ef fective for a wide range of design conditions. The transient test facility provided data that confirmed the results of the analytical model and assurance that the integrated system functioned properly. Tests with noble gas tracers offer encouraging evidence that the pool is ef fective for retaining fission products. e Abs t r a c t -c ont 'd l these facilities are presented in this report. s t e eu., w % rw w.t...d m,* m =.e. s. A.W i.4 s .i,.**.a r i.+.. e 4.ed u,d ta. k s.t.# m:n a..t., pkw,.%. a 4 s me e p.,. (m.aiw). Pacific Gas and Electric Co. j im:wavion e.a.a.co re. and operating personnel of P. G. & E. L A. M. Kennedy, R. Edin,iock, E. Jantsen, A. G. Steaf er, of General Electric. l G. B. Bethards, n. L. F i '+ Enoineerino counts sie=en sectio (300) 129 San.Tose, California w e,,,,,, ,,,,,,e,,,,,,,,,,,_ 4

I The most important single design consideration is the neak pressure in the dry well. This pressure de ermines the design conditions for the dry well vessel. In general, the test results agreed very well with analytical model results. There were, of course, deviations between the two due to various causes such as flow cond!'. ions at the pressure vessel discharge (orifice), and subcooled conditions in the pressure vessel. In all cases, the analytical model results had higher values for peak pressure and sherter time intervals to reach peak pressure than corresponding test coaditions. The peak pressure in the dry well is determined primarily by the break area (pressure vessel discharge conditions), the yent depth of submerge:.ce and the dry well volume. The depth of submergence is the easiest to control by design and various schemes may be used to keep water out of these vents. With no water inside of the vents, the peak pressure is reduced substantially. The vent area (above a certain minimum value for given conditions) has little or no influence on the peak pressure of the dry well. The vent area does af fect the a fter-peak response of pressure in the dry well. It appears that this area may be reduced from that originally contemplated. Dry well design pressures were noted to have high values of negative pressure at the end of the event. It will be necessary to consider thir behavior when designing the dry well. Ancther design consideration is that of pressure in the containment volume. The air expelled from the dry well enters the containnent volume and compresses the gas in the contaimnent volume in what appears to be an adiabatic process. The larger the ratio of containment volume to dry well volume the lower this pressure will be. A significant feature of the entire system is that all of the respective volumes return to essentially atmospheric pressure within seconds after the event. This is an important consideration in fission product leakage. Tests made with xenon and krypton gas samples indicate the system is ef fective for retaining fission products in the pool. / II-2

LEGlBILITY NOTidk[ $~ A major purpose of the Techni-ca Information Center is to provide

- t7e broadest dissemination possi-

'.be of information con':ainec; in DOE's Researc7 and Deveoamen: Reports to business, industry, t7e academic community, and federa, state anc local governments. Al':houg7 a sma portion of this l report is not reproducible, it is . being made avaia3 e to expeci:'e . t7e avaia3ii':y of irformation on t7e research discussed herein.

6- ~ 6EnP-3 /t/.-? f - T'l- /) pf gr April 17,1959 ( Distributian: e D. H. Ahmann L. Ieeen R. K. Andersen A. J. McCrocklin J. A. Bailey P. M. Murphy a K. P. Cohen J. L. Murray W. H. Cook S. Naynark R. H. Dempsey E. R. Owen V. A. Elliott R. B. Richards L. F. Fidrych C. H. Robbins W. L. Fiock J. L. Schanr. L. E. Foster W. Schultheis R. B. Gile G. Sege W. A. Hartman A. G. Silvester M. A. Head J. M. Smith i F. F. Heimann A. G. Steamer H. W. Huntley T. Trocki D. H. Imhoff W. K. Woods E. Janssen Library - 9 W. R. Kanne G.E. San Francisco Office S. Levy Pacific Gas & Electric Co. 4 G.E.R.S.C. Subcouncil 4 PLEASE N(77E: PROPRIETARY INFGMTION e Information concerning pressure suppression should be handled with dis-cretion and should not be discussed outside of the Company. The results g of the development program would be of cocsidemble value to General Electric's competitors concerning pressure suppression. The extent and the method of publication have not yet been decided upon by P.G.&E. and APID. Until this, has been decided, it vo:'.d be best not to discuss pressu-e ( suppression out' aide of General Electric snd to use discretion in discussions within the Company. DISCLAIMER nas report was prepared a an acumunt of work sponsorid by an ageoe) of tae United St.tes Government. Neither the Leited States Government nor any agency thereof. sor any of their employees, makes any war auty, ergress or un;6ed, or assumes an) legal hatut) or resconsi-bihty for the accuracy, comrecteness. or usefulness of any informatioc. appara:u>, prudact or process disclosed, or reprimmt* that its use would not infnnge pnvately owned rights Refer. ence herein to any specific a=nmeraal product, proccu, or sernce by trade name, trademari, manufaaurer, or otherwise does sat accessan'y constitute or unply sts endriement, ruxun-mendation, or favorinF by ac Unned States Government or any agency tht.cof The ne=s f and opinions of authors ceessed h: rein do not necrssanh sate or ref>,c:: ,, -.. ~....... thase of the .. t

IlEEE Esar. I. INTRODUCTION I-1 II. CONCI.USIONS 11-1 III. CONDENSIN3 TESTS Purpose of Tests III-1 Test Proora, III-1 Descript:<.n af Test Facility III-3 Test Prooien e III-5 Discussior. af stesults III-5 Conclusions from Test Results IV. TRANSIENT TESTS Purpose of Tests IV-1 Test Program IV-1 Description of Test Facility IV 2 Test Procedure IV-6 Discussion of Results IV-9 Conclusions from Test Results IV-15 i V. APPENDIX A. Condensing Test Sample Data and Detailed Program B. Methods of Analysis C. Transient Test Data D. Methods of Analysis E. Reference Drawings e 1i } +,- ,-n

1 i ERRATA EEE, Pace No. II-l Line 1, emit "trans *. III-2 Line 7, chPnge Nere" to --was III-7 Line 7, after the period insert -Figure VA-10 is a temperature chart for the bottom horizontal injector run in which steam was released into the vapor space. (The tegerature scale is labeled as megawatts.) III-7 End of fifth paragraph, after the period insert -The temperature chart for the 4 inch multiple injecto; is shown on Figure VA-11. This chart is typical for the vertical injectors. III-8 Line 1, change " smooth" to -smoothly-. III-8 Fourth paragraph, last line, after the period insert -Figure VA-12 is a typical temperature chart obtained during the runs for investigating pool vibration. III-9 Line 7, change

wide" to --wise III-9 Second paragraph, last line, af ter period insert -The intensity of the vibrations increased with increased steam flow rate. under all conditions.

III-ll After paragraph numbered 4, insert --Refer to Figure VA-13 for a typical temperature record obtained with the conpartment tests. It should be noted that only one thermocouple was used to record temperatures of the water in the compartment. It was connected to several recording points. IV-1 Line 3, insert -system-after " suppression". IV-4 Third paragraph, line 6, change "shart" to --sharp. IV-5 Fourth paragraph, line 1, change "p9rtion" to --portion-. IV-6 Fifth and sixth paragraphs, lines 4 and 6, respectively, change "tupture" to -rupture-. IV-13 Second paragraph, line 3, should read --of Figures V;-7 and VC-11 with Figures VC-15 and VC-9,-. IV-16 Third paragraph, line 10, change " air" to --aid Floures V-A-1 to V-A-8 Line 4, respectively substitute -2 MILLISECONDS / DIVISION-- for "10 MILLISECONDS IN3".

4 1. INTRODUCTIOi The test results obtained from the pressure suppression development program provide conclusive evidence that the concept is practical for reactor containneent. A pressure suppression containment system in its simplest form is shown in Figure I-1. The reactor vessel volume, dry well volume and containment volume are labeled as volume (1), (2), and (3), respectively. The water pool for condensing the released steam is part of the containment volume (3). In operation, steam would be released from a rupture in the reactor pressure vessel or the primary coolant system and flow into the dry well volume; the steam is discharged from the dry well, through vent pipes, into the water pool where it is condensed. The salient features of the system are low cantainment pressures and the entrainment of released fission products in the water pool. As with most new conceptr there are many design considerations that can be resolved only with model or prototype testing. Two major test facilities were constructed to obtain the experimental infcrma-tion considered necessary for the evaluation of a pressure suppression system. Pacific Gas and Flectric Co. sponsored a development program that included a large condensing test facility at the Moss Landing Power Plant of Pacific Gas and Electric Co., and a scale model transient test facility at the San Jose Plant of General Electric Co. This report presents the results of tests performed at these facilities. The condensing test facility consisted of a large tank of water with steam headers that would facilitate discharge of steam into the water pool with full size vent pipes of various arrangements. The steam supply system permitted flow rates up to 100,000 pounds per hour. These tests provided data for design of the steam injection equipment and for the arrangement of the water pool. The scale model transient test facility was built to represent a 50 Mw prototype peeer plant reactor enclosure with a volumetric scale factor of 1000 to 1. The facility consisted of a pressure vessel, dry well and a containment tank with a water pool. The facility was designed with the flexibility necessary for obtaining pressure response data with variations of the many des.gn parameters. The results of this test were primarily used to ccnfirm the mathe-eatical model for predicting pressure response of the dry well volume and to evaluate effectiveness of fission produ:t entrainment. w I-l 1 --

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l II. CONCLUSI0riS The results of tests conducted with the condensing test facility and trans-transient test facility were highly successful with respect to verifying and extending the technology of pressure suppression systems for reactor containment. Tests performed with the condensing facility were significant in that, of the hundreds of various tests, steam release could be detected in only three instances. None of these tests,would be considered as reasonable for design condition. A simple' pipe of suitable diameter may be used as a steam injector to accomplish rapid and effective condensation. The depth of submergence of the discharge end is not cr.itical for complete condensation with vertical injectors. With horizontal injectors it is necessary to have sufficient depth of submergence (a few feet) to prevent steam release. Under certain test conditions, there were severe pressure fluctuations in the pool. A series of tests arre run to deterrane the magnitude and frequency of these pressure fluctuations. The conclusions from these 0 tests were that for pool temperatures less than 120 to 133 F the fluctuations were very small and that under any conditions the magnitude could be reduced by supports fastened to the injector. Tests run with an internal compartment to reduce the effective volume of water were important to determine injector-pool geometry relations. The conclusions from these tests were as follows : l. The two dimensional representation of the pool by using the compartments was valid for determining pool geometry. ? 2. Some of the injector-pool geometry cumbinations were better than others from the consideration of pool surface deflectiens and also pool mixing. 3. The air injected into the pool at the onset of the event will not interfere i.th condensation. Further, the air that is slowly purged n out of the Itry well will not materially affect complete condensation of the steah. ? 1 The r suits of f.he transient test facility have provided conclusive evidence that the pressure suppression system is ef fective in containing the energy release from a boiling water reactor incident. Furthermore, the pressure behavior of such a system may be calculated with a reasonable degryse of accuracy, and the values are conservative when compared to the ~ test values. The test results also indicate that such a system will probably be very effective for retaining any fission produ:ts that may be released with an accident. II-1

1 III. CDNDENSING TESTS A. Purpose of Tests The condensing test facility was used to demonstrate and evaluate the condensing effectiveness of steam injection equipment of sufficient size and arrangement that it could be used in multiple units far a full scale pressure suppression system. The specific objectives were as follows : 1. Demonstrate, with steady state steam flow, that rapid and effective condensation may be obtained by a simple straight pipe injector immersed in a pool of water. 2. Investigate the effect on condensation effectiveness of injector part. meters such as; injector diameter, steam flow rate, depth of submergence of the discharge, direction of discharge and multiple jets. 3. Evaluate the condensation effectiveness of single and multiple injectors in a restricted volume of water as a function of the geometry of the restricting volume. B. Test Proaram The condensing test facility program followed, in general, that initially proposed. The major effort of the program was directed towards obtaining data to evaluate the design parameters of the combined injector-pool arrangements. The sequence of testing followed a logical order of shake-down tests, injector parameter tests, including a series of tes+s to i determine vibrational characteristics of the injectors, and compart-ment tests to determine the interaction between pool geometries and the injectors. Initial Tests The first tests were run with a 4 inch Jiameter injector for shake- ~ down and instrument check out. These tests ware run with an open tank and visual operation of the jet behavior. Initial instrtmentation check out and adjustments were made at this time. Group I The first series of tests were to obtain preliminary data for the facility by observing the behavior of steam injected into subcooled water with different flow rates and depths of submergence of the ir.jector. The single 4 inch and 8 inch vertical injectors were used i III-l

-( at depths of submergence ranging from 2.1 inches to 2 feet, with steam flow rates of 15,000 to 80,000 lbs, per hour. These tests were run with both the open tank condition (for visual observation) and the closed tank to obtain evaluation data. Group II Before the full scale parametric test program was begun, a series of tests were run to determine the sensitivity of the test facility for detecting steam release into the vapor space. To do this, h a small orifice directly into the vapor steam was metered throug/4" diameter orifice was mounted to the space. A plate with a 3 14 inch by 4 inch reducer section. Attached to the orifice plate and separated by spacer bars, another plate served as a deflector to diffuse the steam into the vapor space. Flow rates up to 500 lbs/hr were used. Group III The tests of Group III were performed to determine the condensation effectiveness as a function of the injector parameters in a large water pool with steady state steam flow. The parameters include the diameter of the injectors, steam flow rates, depths of submergence, and direction of jet discharge. The nozzles used for these tests were the 4, 6, 8 and 14 inch diameter single vertical injectors, a multiple 4 inch diareter injector, a 4 inch diameter top horizontal injector and 4, 6, 8 and 14 inch diameter bottom horizontal inje _ tors. All of the injectors are shown in Figure III-4. During these tests, l the tank was both open (for visual operation) and closed to determine condensation effectiveness. Depths of submergence ranged from 6 inches to 6 feet with steam flow rates of 10,000 to 93,000 pounds per Nour. QIP9Md..E During the tests of Group III it was noted that severe tank vibrations occurred with some of the test conditions. A series of tests was performed to provide some insight into the magnitude and frequency of the pressure fluctuations that caused the vibration. For these tests, the pool temperatures were varied from 50 F to 0 150 F and the flow rates were varied throughout the maximum range. In addition, the depths of submergence and support cf the injecter proper were investigated. The tests were made using the 4, 6, 8 and 14 inch diameter single injectors and the multiple 4 inch diameter injector. III-2

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Group V To evaluate the condensing effectiveness of the various injectors in a confined volume of water, comparable to that available to individual injectors in a prototype, a series of tests were run with the injectors discharging into a confined compartment that could be varied in width, length, and depth. It was also possible to have various combinations of the width, depth and length. The 4" and 8" diameter vertical injectors and a multiple 4 inch diameter injector were used for these tests. The multiple injector was mounted in both the tandem and side-by-side positions. The tandem t position is shown in Figure III-3. The side-by-side position was with the compartment 18" wide and the line of injectors parallel to the width of. the compartment. The 4" and 8" injectors were used with 6" and 12" wide compartments, respectively. C. Description of Tes t Fa cili,1,y. The test facility was located at the Moss Landing Power Station of the Pacific Gas and Electric Corupany. Figures III-1 and III-2 shcm. g the general arrangement of the facility. The basic tesi. chamber was a tank 20 feet in diameter and 24 feet high with dished bottom and top. Figure III-3 is a cut-away isometric view of the facility showing the major details to be described. The top was penetrated by the following: 20" diameter manhole, a 3" vent valve, pressure relief valve, rupture diaphrag.., 3 thermocouple leads for measuring temperatures inside the tank, and 4 glass windows for observing the inside of the tank. The side of the tank contained a 6' diameter hatch for equipment, water level 9 age connections, two 14" diameter steam inlet headers, two 1-1/2" connections for filling the tank, a 4" drain and 14 glass viewing . ports. Attached to the exterior wall were a ladder to the top, and two platforms so personnel could look through elevated windows. A standpipe was attached near the bottom of the tank to control normal water level and to provide an overflow line for condensate during testing. Four flood lights of 500 watts each were used to light the interior of the tank. The interior of the tank was painted white for better visibility. Steam was supplied frort two existing 8" - 100 psi stear lines. Headers from these lines connected to a single 10 inch line which contained an orifice for measuring steam flow. An 8 inch angle valve located S feet from the base of the tank was used for flow control. After the valve the line branched to enter the tank at elevations of III-G I

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l' - 6" and 22' - 6". Both lines were 14" diameter. Special combination ring-blind flanges were used in the tee at the bottom to prevent steam flow to the unused header. The 8" control valve was bypassed by a 2 inch line containing a flow control valve and two drain valves. The bypass valve was used for flows under 1000 pcunds per hour. Instrumentation for the compartment tests consisted of windows for visual observation and static pressure taps on the side of the compartment, and one thermocouple located just below the water surface (supported by a wood float) at the end of the compartment away from the injector. The static taps were used to measure surface deflections. Both still-sequence pictures and movie pictures were used to record the pool and jet behavior within the compartment. Basic instrumentation was that necessary to measure the pressures, temperatures, wat er level and steam flow. Figure III-3a shows the instrumentation line ciagram. Stea.a flow into the tank was measured in the line before the flow orifice and in the 14 inch line just before it entered the tank. Steam pressure downstream from the control valve was also measured. After testing had begun instrumen-tation was added to measure steam pressure at the discharge end of the steam injector pipes. L Vapor space instrumentation was for the purpose of detecting incomplete condensation of steam with e closed tank. A water level gage was used to determine the vapor volume above the water pool, 3 thermo-couples were used to meesure the vapor space temperature, and the pressure in the vapor space was measured with a mercury manometer. The group II runs were made to determine the sensitivity of this means of detecting steam release. However, it was subsequently established that small amounts of steam released to the vapor space when the tank was open could be readily detected because of fog formation. Most of the tests were run with the manhole at the top of the tank open for visual observation. Water temperatures within the tank were measured with 3 thermocouples located in the side of the tank. All 6 thermocouple temperatures were recorded by a 16 point per/ minute Speedomax Recorder, with i repeating preference given to those considered most important for a particular test. For the tests with a confined pool volume, a compartment was I fabricated with over-all dimensions of 12' long,12' deep and 18" wide. The compartment was so arranged that the following variations l in dimensions could be obtained: III-4

Width: 6, 12, 18 inches Length : 4, 6, 8, 10, 12 feet Depth : 6, 8,10,12 feet Any combination of these dimensions could be used. Glass view windows were located on the sides of the compartment to observe the surface of ths pol near the injectors and the steam jet at the injector oischarge. The conpartment was positioned and supported on a frame that could be relocated easily within the tank. Test Procedure The standard p' actices for operating this type of experiment, r such as tank filling, steam warm-up, and instrument checks, were followed in preparing for testing. A minimum of three people were required to run the tests. The operator manipulated the steam control valve, filled and drained the tank and warmed up the system for testing. In addition, he was occasionally called upon to record data. The recorder ~ transcribed the data from the instruments to a log at specific time intervals and directed the operator's activities. The observer maintained positions on t p of the tank, on the ladder, or on the platforms and recorded the reactions within the tank. For the conpartment tests, the operator was requested to spin the control valve open quickly and set the required flow for the duration of the run. Some of the runs were as short as 20 seconds. After each run, cold water was punped into the compartment with a fire hose to prepare for the next run. Most of the runs with the compartment were recorded with movie and still-sequence pictures. The facility was secured in the manner requested by plant of ficials as would befit any facility of this type. C. Discussim_of Results Group I These tests were performed to observe the effect of large flow rates of steam being injected into a pool of subcooled water, and to set the practical operating limits of the facility. The initial test was carried out with the single 4 inch vertical injector. Depths of submergence used were 6 inches and 1 foot. Steam mass flow rates to a maximum of 53,300 lbs/hr were injected. Jet flow through the injector was observed at 14,200 lbs/hr. There was no evidence of release of steam from the pool during the test at either depth of submergence or at any of the mass flow rates. The preceding operation was repeated with the i 8 inch injector at mass flow rates to 90,000 lbs/hr with the same results. l 777-5

Prom the results obtained it was concluded that the facility was adequate and needed no further mod!fication. Some of the highlights of the visual observations provide interesting aspects in further describing the reactions in the pool. During the operation of the single 4 inch vertical injector in the open tank run, the pool surface was carefully observed. As the mass flow rate increased, the agitation of the pool increased. At 30,000 lbsAr (recorded) small vortices appeared arourr$ the injector for approximately 10 seconds and then disappeared. A few seconds after the small vortices disappeared one large vortex began forming around the injector and as best one could see extended just below the injector. This la +ed about 10 to 15 seconds followed by a tremendous upheaval around the injector. This, of course, was the release of the air that had been drawn down the vortex. With the 8 inch vertical injactor installed and a mass flow rateof70,000lbshronlythesmallvorticesaround the injector appeared. These collapsed but never formed into one large vortex. Grouc II These tests were performed with a 3/4 inch orifice (See Figure III-4) installed on the 14 inch header and a sealed tank. To establish cendensing effectiveness it is impor : ant to be able to detect and if necessary measure, any significant steam release to the vapor space above the pool. Part of any steam released would be condensed on the tank vtalls and top, and on the pool surface. Results of the test using the orifice to meter steam directly to the vapor space show that the rate of condensation is negligible (less than 500lbs/hr). Calculations show that any significant amounts stearr released to the vapor space will cause rapid and substantial increases in both pressure and temperature. 1000 lbs/hr will cause the pressure to rise about 1/2 psi 0 per minute and the temperature about 13-1/2 F per minute. i The tesperature chart for this run is shown in Figure V A-9. Grouo III These tests were performed to determine the relationship between injector geometry and condensing ef fectiveness. The tank was open during the first tests of each injector and then closed for the remaining tests. The first tests were for visual observations of the reaction at various flow j rates and depths of submergence. The remainder of the tests, during which the tank was closed, provided da.a that con-curred with the visual observations indicating whether or not steam was released. The only indication of steam III-6

. - - - _ - - =.. - l } l release occurred during the tests with the 6 inch and 8. inch bottom horizontal injectors at 6" depth of submergence. 1 i This could be visually observed during the tests at the higher mass flow rates when the momentun of the jet leaving the ] injector was so great that it carried across the tank before completely condensing and the splashing against the wall of the tank released some of the uncondensed steam. 1 3 With the 6 inch single vertical injector vortices first appeared at a mass flow rate of 48,400 lbs/hr. The vortex lasted about 10-15 seconds and then collapsed followed by j the upheaval of air through the water. The mass flow rates 1 were held for about one minute but the vortex did not reform. At each 5,000 lbs/hr mass flow rate increase vortices formed i and collapsed. The vortices were not self-sustaining at any mass flow rate. At a maximum mass flow rate of 83,300 lbs/hr, i agitation of the pool was severe and the direction of flow 1 of the pool surface was from the far wall to the injector indicating the type of circulation apparent in the pool. During a run with the 4 inch single vertical injector, rate of 56,000 lbs/pth of submergence and maximum mass flow ! closed tank, 6" de t hr, the tank was quiet during the first j 16 minutes of operation. At this point, the pressure in l the tank rcse to about 6" mercury due to the accumulated condensate and the. tank v..enced shaking. Two minutes later, the tank began to shudder and then bang severely. j This banging literally sounded like rapid fire from a i rifle. After 5 minutes of this the vibration was severe i enough to shake open the safety relief valve and the run was i secured. It was concluded from this run the t the peel vibration phenomenon was tegerature sensitive and that the frequency and magnitude of the vibration should be investigated. I j The 14 inch inyctor was too large for the steam supply i available. At the low line pressure it was not possible to obtain jet flow with this injector and chugging occurred. l nith the tank closed, shaking and banging occurred but the intensity was less severe than that of the sma'ler injecters i l with higher velocities. i The 4 inch multiple injsetor provided the smoothest running 1 of all injectors tested. Tge tank began to shake as the pool tegerature neared 150 F but the intensity was very low. l The 8 inch injector reacted essentially the same as the other injectors in causing shaking and banging in the tar.k. During the second run of this series at a mass flow rate of l l 77,500 lbs/hr, the water level was dropped, via pumping, to observe at what depth of submergence steam would be released. Steam blow by was observed at la depth of submergence. l I III-7 ~f i i

The 4 inch top horizontal injector ran smooth during the runs at lower pool temperature with 6" depth of submergence. At 6' depth of submergence it became somewhat rougher as the water temperature increased. The bottom 4 inch injector operated the same as the previously run top horizontal injector. The operation was smooth at 6" depths of submergence and gradually increased in roughness at 6' depth of subr..ergence as the pool water temperature increased. The operation of the bottom 14" injector proved to be a serious problem since the steam line ran horizontally l from the control valve into the tank. nith hot steam on one side of the valve and cold water on the other, a.ong with insufficient pressure to produce jet flow, the r water hammen was quite severe. The tank shook severely during the run which was made at 6 inch depth of submergence with the tank open. As the steam valve was being closed, at a slow rate, the severity of the water hammer increased to a point where everything in the vicinity of the tank j was shaking. I Groue IV The 4, 6, 8 and multiple 4 inch injectors were each ratested. i This series cor sisted of tests with each injector rigidly j connected to the tank wall at a point midway over the length of the injector and corresponding tests with the rigid connecticn removed. These tests were run to investigate the effects of various parameters on the magnitude and frequency of the pool pressure fluctuations generated by the i discharge of steam. An oscilloscope with a cemtra was used to record the output of a pressure transducer mounted in the i tank wall at approximately a S' elevation in line with the injector. In each case, the runs consisted of going from i maximum mass flow rate to zero in increments of 15,000 lbs/hr in a cold pool at 6' depth of submergence. Then at maximut. l mass flow rates, the pool was heated. After maximum pool l temperature was reached the mass flow rate was reduced by l 15,000 lbs/hr increments. The depth of submergence was then I, lowered to 4'. Mass flow rates of 105,033 lbs/hr and 75,033 l lbs/hr recorded were used. The depth of submergence was i lowered to 2' and the process repeated. Photographs from 0 the scope were taken at each mass flow rate and at each 10 F l tenperature rise during the heating run. Figures V A-1 throug' V A-8 are a conplete series of photographs taken during the test of the 8 inch vertical injector anchored and unanchered, i i 1 III-6

During the operation of the 6" injector anchored to the tank wall and specifically during the run where the mass flow rate was being reduced following the heating of the pool,. the facility became so rough that the tank appeared to be bouncing on its foundation. Personnel in the control room of the power station recorded a mild earthquake which time-wide coincided with this run. Photographs taken during this run show peak pressure fluctuations of 6 psi, while photographs taken when the anchor to the tank wall was removed show peak pressure fluctuations of 10 psi during the same run with less severe reaction of the facility and no bouncing of the tanh. In this sa.e on nchored series, at 4' depth of submergence and recorded mass flow rate of 10t,000 lbs/hr, the peak prebsure was 24 psi as compared to 3 ps* when anchored. At 2' depth of submergence a peak pressure of 40 psi + as compared to 6 psi then the injector was anchored. It was observed during the entire series of tests in thig group, that as the pool teraperature reached 120*F to 130 i-the roughness commenced and increased in intensity with the increase in tenperature. The operation of the facility was amooth in all cases as long as the pool temperature remained below 120 F. t 9 e III-9

s Comoartment Test gesults Speaking generally of the crepartment tests, the pool surface i within the confines of the compartment walls was much more agitated than had previously been observed with the same injectors l discharging into the large pool. There was no tendency to form vortices, but the surface in the neighborhood of the injector tended to be depressed below the surroundings. A typical example of this behavior is pictured in Figures III-6 and 111-7, which are top and side views, respectively, for run No. 54 (the first three pictures in each figure were taken before the steady state pattern was established). The surface typically had a very foamy appear-ance, particularly at the injector end of the compartment and at the end opposite the injector. Water flowed down from the end opposite the injector toward the injector end; there was a small jump just before it reached the injector. The viewing windows in the sides of the compartment permitted a relatively clear view of the jets which foreed at the injector discharge. For each run these jets underwent a characteristically changing pattern. gone of the characteristics are shown in Figure j 111-5. Ficture 1-No flow. Picture 2: The first puff of steam appears. Fictures 3 and 4: Full flow but the jet is very short (in this case, about 4" to where it " necks down". The calculated velocity for this picture was $35 f t. per sec.), associated with high subcooling. Fictures 5 and 6: The jet becomes longer and is l 1ess " necked down" as the pool subcooling decreases. Ficture 7: Apparently slightly underexpanded jet, low subcooling (calculated velocity for this picture was 1000 f t. per sec.). The jets some-times tended to draw together as shown here. Ficture 6: Shutting down. Note in the last four pictures the formation of air bubbles in the bulk of the pool to the lef t of the jets. These appeared as the water temperature was approaching 150 F They are presumed to be initially dissolved air which had been driven out of solution. The results of the compartment tests are summarized in Tab 1c I,. (except for qualitative observations of the effect of air on con-densation, which will be described later). Columns are arranged to give, for each run, geometry, steam flow rate, and two quantite-tive measures of performance, viz., surf ace de 'ection, and mean temperature rise (calculated) versus temperatu' ise at a point (measured). The following notes are intended to better identify some of the quantities. 1. " Injector - Distance From gnd" is the distance from the end of the compartment to the center of the injector (to the center of the nearest nostle in the case of the triple injector). 2. " Rates - Mass" is the Barton Flow Meter reading corrected fer steam conditions dif ferent than rated. For runn 84 through 91 the single 4 inch injector was itself calibrated (the minimum flew which can be measured satisfactorily with the Barton Meter was too great for these runs) tu give mass rate as a function l ciap across the injector and the state of the steam directly upstream. 111-10 i

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TABLE 111-1 COMPARTMENT TEST RESULTS j Coupartment Iniector Rates Deflection Temp.Ris e Sub-Diet

CALC, Run Length Depth Width

w rge From Size J Jissa Velocity MON.

M&M. CBS. MEANMAS. No.' (ft) (ft) (ft) (QL 8:nd f f t) 1b/see) (ft/sec) (1b) (ft) (ft) (OF) (DF) 1 12 12 1.5 6 0.7 4" 17.1 1470 775 51 52 2 18.2 1510 840 3.0 39 49 3 20.7 1580 975 64 49 4 23.7 1610 1115 66 40 5-10 12.4 1310 470 21 30 6 14.4 1340 600 53 31 7 16.7 1450 755 76 52 8 l'L / 1:: 0 Ce 9 18.7 1530 830 75 59 10 20.2 1560 945 66.' 56 11 21.9 1590 1940s 1.2 76 56 . 12 4 7.8 785 190, 0 46 42 ' 13 10.3 1035 330.. 0 52 25 14 12.8 1230 490 46 30 15 16 17 8 11.2 1110 385 0.6 64 58 18 13.3 1265 530 0.8 58 36 19 16.6 1450 745 1.1 64 64 20 18.3 1510 850 1.4 63 65 21 20.4 1570 960 1.7 79 63 f 22 10 13.3 1265 530 1.8 91 66 23 18.6 1525 895 67 40 24 25 12 9.7 965 290 0.1 29 33 25 13.5 1280 535 0.3 59 54 27 19.5 1550 915 0.3 54 38 28 8 9.4 935 275 0.1 36 48 29 13.4 1275 535 0.2 44 46 30 19.0 1535 885 0.4 59 32 31 8 8 1.5 6 0.7 10.3 965 310 0 81 0 32 14.8 1230 565 0.1 150 6 33 20.1 1420 885 0 137 3 34 12 12 0.5 35 5.3 539 87.5 0.5 0.2 44 45 I r I

l III-I (Continued) j Comp ar tment Iniector Rates Deflection Temp. Rise Sub-Dist CALC ngth D pth Width merge From Size Mass Velocity MOM. MAN. OBS.MEAN MEAS. t) (ft) (dt) (ft) End(ft) [1b/sec) (ft/sec) (1b) (ft) (ft) ( F) ( F) Triple 12 12 0.5 6 0.7 4n 10.2 1110 355 5.0 1.2 67 42 15.0 1425 665 7.3 72 27 8 5.3 540 89.5 0.6 0.2 47 34 10.3 1155 370 3.0 0 77 39 14.6 .1435 650 4.2 118 42 8 5.3 530 87.0 161 78 Triple 12 12 1.5 4" 5.3 525 86.5 0 0.2 13 22 side 10.2 1005 220 0.2 25 34 by side 14.6 1320 600 1.0 1.2 40 25 8 5.3 520 85.5 0.1 0.3 22 25 10.2 1000 315 1.0 0.5 28 32 14.6 1325 600 1.4 2.2 12 8 5.3 S15 85.0 0.1 0 20 26 10.2 995 315 0.3 0.4 31, 32 14.6 955 433 1 ' ' O. ) 64 44 8 5.3 495 '8'.5 C 0.2 34 44 10.2 975 ' lo u.7 0.8 35 44 Triple 14.4 129 >bt 1.6 1.9 100 107 12 12 0.5 4" 5.4 53s 90.5 0.6 0 58 43 73 805 195 1.5 0.3 80 60 IJ.2 1000 320 1.6 1.5 74 40 12.5 1210 475 6.1 2.5 h] 66 65 14.4 840 375 4.2 8 5.4 535 90.5 1.0 o 158 76 7.8 715 175 1.3 0.4 199 75 10.2 950 300 2.3 2.5 12.5 1230 480 3.0 2.5 136 72 14.7 1260 575 3.7 2.5 236 75 5.3 515 85.5 1.8 0 44 87 7.9 770 190 2.1 b?8 66 77 10.2 835 265 5.2 {35 Se 101 12.6 1030 400 7.5 .0 129 97 8 5.3 545 90.5 1.7 0 69 91 6?$;tti 7.8 740 180 3,3 tot 10.3 1065 340 1.7 ,7 ' 60 7S I 0 12.6 1045 410 4.0 '. 0 260 g L2 ' ~ 12 12 3.2 5.3 540 89.5 1.0 0 10.2 1075 340 2.5 03 52 ! 25 1.8 10,0 475 3.0 0 13; $0 = l (

Tablo III-I (Continued) N <'1 Compartment Injector Rates Deflection Temp. Rise Sub Dist CALC. Kun Lcagth Depth Width merge From Size Mass Velocity MOM. MAN. OBS HEAN MEAS. So. (ft) (ft) (ft) (ft) End(ft) (1b/see) (ft/sec) (Ib) (ft) (ft) (OF) ( F) 16 8 8 1.0 4 0.7 SE *

5.3 415 68.5 0.2 0

55 47 19, 10.3 705 '225 1.9 75 54 58 30 14.8 990 655 3.1 Svgr 80 68 31, 12 12 6 5.3 390 64.5 0.4 0 18 27 32 10.3 740 240 0.6 0 19 22 33 15.2 1030 485 1.9 };6 30 16 34 6 6 0.5 3 siggle 35 1.1 340 11.5 -0.4 0 36 3.3 810 81.5 -0.8 0 37 5.8 1030 190 1.5 0 190 36 38 12 12 6 39 10 3.0 755 70.5! 4 0.5 11 14 71 5.1 1095 173 0.8 2.0 29 15

e s.q a " Rates - Velocity" is the calculated velocity at injertor exit. " Rates - Momentumf' is the product of mass rate and velocity. The bases for these two calculations are given in Appendix B. The method of calculation could not be applied to runs 1 to 30, because no pressure at injector exit was measured. Velocity as a smoothed function of mass rate was determined, based on all the subsequent runs and then applied to runs 1 to 30. 3. ' "Dcflection" refars to pool surface deflection 'in the com-partment. It is the amount that the surface in' the region of the injector war depressed below the surface at its highest point. This proved difficult to determine by direct observation. For run 35 and af ter, another indication of this surface deflection was obtained by measuring the difference betwe in the static pressure below the surf ace at the injector end of the compartment and the static pressure below the surface at the end opposite the injector. The measuring instrument was a manometer, hence, the column head-ing assigned to this quantity is " Man." Values determined by direct observation are in the column headed "Obs." 4. " Temperature Rise - Calc. Mean" is the calculated temperature rise for the water in the compartment from e consideration of heat capacity and net rate of energy ad?ition. The basis for this calculation is Eiven in Appendix E. " Temperature Rise - Messt. red" is the temperature rise measuted at a point lucated just below the surface and er the end of the co:r.partment opposite the injector. Visual means were employed to check for stea:n release during the compartment test. No release of injector steam was detected for any of the runs, although some fog formation was observed near the end of sorae of the runs. In these cases the compartnent water temperature was approaching boiling. The duration of the compartment runs varied from about 20 seconds (Run #85) to.about 100 seconds (Run #2). Although a few seconds were allowed after the beginning of each run for the instruments to come to equilibrium, the data is undoubtedly affected by the time response characteristics of the instruments, particularly for the shorter runs. The pressure regulating system on the steam supply itself has a relatively slow time response (of the order of 15 seconds) which further affected the data. The compartment flow pattern, temperature, and volume ' occupied by vapor (.sssociated with decreasing subcooling), were all in a transition state, further complicating the problem of securing (and interpreting) data. The final effect of the response char acteristics of instruments and pressure regulation, and the transient character of the compartment phenomena was a scattering of da:a which carried over into the results in Table I. Any cumulc?ive effects are impossible cf detection; it is believed that they are minct. 111-11 m y i +w c-,- e--- ,ew cy, .ry-,e, e-, --w -w.,- ,--,.,v- ,,, - -,,_-e,--.,ar--- -r---v-- ---w-r-*--------

During.some of the runs, a general receding of the surf ace in the compartment, of as much as a foot at the highest fleu rates, was noted. This must have been due to the region of high pressure directly below the injector discharge plus the presence of holes and cracks through which part of the compartment contents could leak out. This outflow at the bottom of the compartment could ~ alter the flow pattern, and certainly would reduce the compart-ment heat capacity. Both these effects are considered small and have not been taken into account in reducing the data. They probably contribute a small amount to the scattering of the results already referred to. The surf ace deflection as indicated by the manometer reading is usually not in agreement with (though in general it shows the same trends as) the directly observed surf ace deflection. The static pressure sensed by the instrument and the hydrostatic pressure corresponding to the surf ace elevation would not be expected to be equal, because of the presence of a velocity head and because of the rotational, turbulent, highly dissipative character of the flow. It was anticipated that the relationship between sensed static pressure and surf ace elevation might be very nearly the same at one end of the compartment as at the other (i.e., the velocity, hence, the velocity head, should be of the same magt.itude, etc.) If this were se, the nxmmeter readings and the direct observations would agree. It appears, theref ore, that the relation-ship cetween sens.ed s:atic pressure and surf ace elevatien ar e not the saec at tbc two ends cf the compartner.t. However, roae cf the lack of agreement can be attributed to the scattering (already mentioned) which all the data was subjected to in greater or lesser degree. The relative agreemc, tends to be better at greater deflections. At all deflectio. 4 greater than abcut 3 feet the manometer ceflection exceeds the directly observed deflection, a happy trait from a saf eguards point of view. More than this, the manometer deflection correlates much better with the mass and i i l momentum rates. For the foregoing reasons, the manometer deflection is taken as the measure of surf ace deflection in the subsequent discussion of results, f It will be noted that for a few of the runs a part or all of the results are missing. This is simply due to the f act that the cor..sponding data were obviously of doubtful accuracy, or the c.c.a were obtained under uncontrolled conditions (e.g., runs 15 .nd 16 during which the baf fle forming one end of the compartment troke loose). l The effect of air on the complete condensation of the steam which would follcw it, under conditions which would exist in a complete and f onctiening prerture suppression system, was investigated qualitatively. The 14" pipe between the steam valve anc the injector (see Figure 111-3 and description of Condensing Tank F cility) was initially filled with air (Runs 76 and 77). The steam valve was 111-12 l l t

opened as quickly as possible to a set flow, and the manner in which the air escaped from the pool was observed, visually, with still pictures (see Figure 111-8), and with moving pictures (Rcct 44, 64 frames /sec.) These observations demonstrated that all the air, except for stum very small bubbles (estimated at less than 1/4 inch diameter) escaped to the surface in of the order of 1/10 second. The time was l .too short for the bulk of the pool water to be set into motion. The air broke the surface directly above the injector exit. ( What was possible to observe of the behavior of the f.ool in the Transient Test j Facility, both visually and with 64 frame-par-second movies, fitted this same general pattern. No circulatini m:. tion was obser vable just. prior to air breaking through except for a slight heaving of the su-f ace. j The violence of the actior. upon breaking the surface then caused the view to be obscured, making further observation of air escape irpossible). During same tests run earlier and reported in the Phase 1 Report, s t.2 e.r containing small amounts of air was discharged into a pool of water. Here the air coalesced at many points tc. form small bubbles, which then I approached the surf ace relatively slowly. Discussion of Conpartment Test Results One criterion foi the adequacy of any pool-injector combinaticn is the complete condens. tion of any steam dischacged into the pool. Tr.e coa.- partment test was to establish the range of parameters fer which this criterion would be met. Rciative to thc ettect of air on the congleteness of condentatico, 't may be stated that ary air being driven in large quantitles frou. the dry well and injected into the po:1 will escape rapidly from ths pcol. so it cannot affect the mechanism of condensction except for a briet inter-val of time. The Transient Test Facility containment pressure data reveal no evidence of uncondensed steam. On the other hand, air i n.nected into the pool in small quantitics will become dispersed as scall b.t.51e 3 which will have time to reach thermodynamic equilibrium before crea'<ieg the surface. Hen:e they can carry no more vaper than that carried by saturated air. No more can be said on the basis of these test results concerning the effcet of air on condensation. When the injector is dischargir.g steam into the pool the pool sarface is disturbed. If it should be depressed 6.. the region of the injecter by an amount apprcximately equal to the original injector submcrgence. steam may be released. One necessary condition for meeting thir criterion for adequacy, then, is that the pool surface must never se dentessed below the iniector exit. If the subcooling drops to near zero along any possible steam bubbic path to the surf ace, steam me, be released. Let the highest tempo a-ture at which coeplete condensation is assured be Tc. A second c or-dition for cettirg the criterion of adequacy is: ther

mus t be ne relatively cent inacus rerions extending fr om the iniectsr _eyit to the surf a:e of the p0.,1, at teerc i atures above 1e.

111-13

The Table I summary of the compartment test results may now be examined in light of the two conditions just stated. First, evideace is desired to show that the flow pattern is a reliable two dimensional representation of a aure extensive system. A comparison of the triple 4 injector arranged side by side in an 18" wide compart-ment, with the single 4" injector in a 6" vide compartment provides such evidence. Surface deflection A a is plotted versus mass rate per foot of compartment width for runa 43, 44, and 45 (triple 4" injector,12' x 12' compartment) and for runs 90 and 91 (single 4" injector,12' x 12' compartment). The plot is shown in Figure 111-9. (As a matter of interest the data obtained by direct observation are also plotted). Surface deflection is plotted versus mass rate in Figure 111-10 for the triple 4" injector in the 6" wide compartment. The depth of submergence is 6' in every case. From a consideration of the first condition for adequacy (i.e., surface depression must be less than injector submergence) the 12' x 12' compartment with injector 3.2 feet from the end is best. An extrapolation would give approximately 50 lbs/sec f t. before surf ace deflection would equal depth of submergence. The 8'L. x 12'D. is next (42 lbs/see ft before o a e depth of submergence), the 8' x 8' next (40 lbs/sec ft before 25z depth of submergence), the 12' x 12' next (27.5 lbs/dec f t before Az. depth of submergence), and the 12'L. x 8'D. Last (22 lbs/sec f t before A z : depth of submergence). It should be pointed out that in the condensing test f acility, surface deflection and surf ace depression are equal (except for a few cases where the wholt surface was depressed as mentioned earlier). In an actual system, however, no water could spill over the walls of the compartment so that for every depression of the surface in one region Chere would be an elevation of the surf ace ~ in one or more other regions. Surface depression would always be Icss than surf ace deflection as defined here. However, for the purpose of comparing compartments, surf ace deflection is as satisf setory as surf ace depression would be. It should also be recalled that surface deflection (as used in the above discussion) is based upon surface deflection as indicated by the difference in static pressures measured at the two ends of the compartment. The agreement between observed surface deflection and surface deflection as detenmined above is usually relatively good at high mass rates. For example, refer to Table 111-1, run numbers 58 and i 59. The " observed" surf ace deflection was known to be between 2.5 and 5.0 feet (the surface was actually below the top window and above the bottom window, hence could not be observed directly), for both runs. The indicated surface deflection for run number 58 was 6.1 feet, slightly outside, but on the conservative side of the limits determined by obser-vation. The indicated surface deflection for run number 59 was 4.2 feet, which is nicely bracketed by the limits set by observation. The agree-ment is worse in some cases and better in others, though the general tendency is for the indicated deflection to be greater than the observed deflection, and therefore conservative, at the higher flows. 111-14 1 l 1

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It mev be argued that good agreement between calculated mean tempera-ture "ise and measured temperature rise at a point is evidence that the mixing is good. It is not conclusive evidence, but provides at least a basic.*or comparing compartments. Good mixing is insurance that the second c ndition for adequacy (no relatively continuous regions at temperatures above Tc) can be mat. The ratio of measured temperature rise to calculated mean is plotted versus mass rate in' Figure 111-11 for the triple 4" injector in the 6" wide compartment. The ratio is positive for the 12'L. x 8'D. compartment for most flow conditions, correspond- ) ing to a higher measured value than the calculated mean. There must have been some streaming action which caused a high temperature stream to flow past the thermocouple used for temperature rise measurement. This l is a situation to be avoided per the second condition for meeting the criterion of adequacy, particularly in visw of the thermocouple's loca-tion near the surface. The ratio of measured to calculated mean temp-j erature rise for the remainder of the compartment sizes, except for J the 8' x 8' compartment at flows less than 15 lb/sec per foot, is less 1 than unity. There appears to be little to choose between these remain-ing compartments. At flows of 20 lbs/sec per foot of width the ratio is approximately 0.5. The ratio increases consistently as the flow decreases toward zero, and in the case of the 12' x 12' compartment it actually appears to be approaching unity at sero flow. Speaking generally of Figure 111-11, there are a few points which are wild and must be questioned, but for the remainder there is a reassuring consistency which argues that mixing is such better at lower flows. It is to be noted that the time when good mixink is important is when the flow is j low. This would be the si*.uation af ter peak response in an actual pres-l sure suppression system, when the steady absorption rate of energy would be causing the pool temperature to increase. ( gurface deflection is plotted versus mass rate p.r unit width in Figure i 111-12 for the single 4" injector, the single 8" injector, and the triple 4" injector in side by side arrangement. The depth of submerg-ence for the single injectors is just half the compartment depth; for the triple injector the depth of submergence is 6 feet. The results i for the single 4" injector'in the 6' x 6' compartment are at variance with the rest of the data and with what shocid be expected. Neglecting l the 6' x 6' compartment data, the remainder of the data is relatively consistant. Although there is not enough data to conclusively establish which compartment is best (the mass rates were much too low to deprecs the surface close to the injector depth of submergence), the 12' x 12' with any one of the three injectors tends to be better than the average, whereas the 8' x 8' with either the single 8" or the triple 4" injector tends to be worse than the average. The ratio of measured temperature rise to calculated mean for the in-jector compartment combinations of the last paragraph are plotted versus mass rate in Figure 111-13. svidence of the streaming action, observed for the triple 4" injector in the 8" deep compartments, is seen for every injector-compartment combination here except the single 8" in the 8' x 8' compartment. (The single point for the single 4" in the 6' x 6' compartment is inconclusive). It is particularly evident at low flow in the compartments of 12 foot length. 111-15 w

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1 ) Apparently the triple injector (nozzles in line with the compartment) in the 12' deep compartments gives much better mixing than do any of the single injectors (or than the triple injector with nozzles arranged side by side, which is the two dimensional equivalent of a single injector) in the same compartments. It must be pointed out, however, that the triple injector was not tested at as low values of mass rate I per unit width. It has not been established that the triple injector gives superior mixing at very low flows. At low flows in the 8' deep compartments the single injectors appear superior. Conclusions From Compartment Test Resulto From the results of the compartment tests as described in the preceeding section, the following conclusions may be drawn: 1. Air driven from the dry well at high mass rates, as would occur in an actual system early in the series of events following a maximum credible type accident, and injected into the pool, will escape rapidly from the pool (in about 1/10 second for injector submergence of 6 feet), so cannot affect the snechanism of con-densation except for a brief interval of time. 2. Low mass rates of air injected into the pool sinultaneously with steam, as would occur in an actual system insnediately af ter the initial peak response, will become dispersed as small bubbles which will have time to reach thermodynamic equilibrium before escaping to the pool surface. 3. The two dimensional approximation of an actual injector-pool com-bination may be simulated in a compartment having a width of 6 inches, within the accuracy of the data reported here. 4. From a consideration of the first condition for adequacy (surf ace depression less than injector submergence), for the triple 4 inch injector at relatively high mass rates (greater than 15 lb/see per foot of compartment width, say), the 12' x 12' compartment with injector 3.2' from the end is best; the 8' x 8' next; the 12' x 12' next; and the 12'L x 8"D. compartment is poorest. (The single injectors were not tested in this range of mass flow rates, so no e conclusions can be drawn concerning their performance relative to the triple injector.) At relatively low mass rates (less than i l 15 lb/see per foot) all injector-compartment combinations gave comparable (and adequate) performance, although the surf ace deflec-tion with the 8' x 8' compartment tended to be greater than with the others. 5. From a consideration of the second condition for adequacy (no relatively continuous regions at temperatures above Tc), with particular concern for low mass rate conditions, and on the basis that the temperature measured at a point near the surf ace should be in good agreemer.t with the calculated mean, the triple 4 inch injector with the 12' x 12' compartment is best, with the 8'L.x12'D. next best, with the 12' x 12' and located 3.2' from the end soce-i what uncertain, and with the 8' deep compartments the poorest. 111-16

On the same basis all the single injector-compartment com.binations were poor coeparad with the triple injector. (The foregoing conclusions concerning uniformity of temperature are only tentative for the following reasons: (a) good agreement between temperature measured at a point and calculated mean temperature is not conclusive evidence that the temperature is everywhere uniform. In particular, it does not insure that there are not relatively continuous regions, removed from the thermo-couple location, which are at temperatures higher than the mean; (b) the temperature measured at one point near the surface may not. be representative of the entire surface. In particular, continuous regions of high temperature water whose possible existance was admitted in (a) could extend to the surf ace; (c) it is particularly important that the temperature be uniform at low flows. No data was obtained at flows less than 10 lb/see per foot for the triple injector, or 3 lb/sec per foot for the single injectors). O l 9 O I ^ 111-17 i

IV. 'IRAESIINT 'IESTS A. Purpose of Tests he primary purpose of the transient test facility was to demonstrate, with a working scale model, the effectiveness of the pressure suppression to contain and absorb the energy and radioactive materials released from the ruptun of a nactor P n ssure vessel or associated primary piping. To this end the specific objectives were as follows: 1. W obtain transient pressure data as functions of the major l system parameters that'vould confirm the analytical model or to provide the basis for improving it. 2. To provide pressun Naponse data not specifically included in the analytical model such as; the pressure decay behavior of the dry well and the containment volume. 3 h evaluate the effectiveness of the system to tre., and retain fission products that could be nicased from ruptun or meltdown of the fuel elements. B. Test Program he test program followed, in general, that proposed in the Phase I report. he major deviations were to accommodate imposed te6t conditions and to expand certain areas of test Esta. he actual test schedule is given in Table.IV-1. Most of the early tests were run and nrun to establish satis-factory methods of ruptur1ng the discs and maintaining saturated conditions at the bottom of the pressure vessel. Rese tests also were used to determine the necessity of additional instru-mentation such as dry well and containment volume thermocouples and the differential pressure transducer between the dry well and containment volume. A comparison of the p.,,osed test program and the actual progra-indicate the deletion of several test points. Most of these tests were those to be run with different' amounts of water in the pressure vessel. It was concluded that the initial amount of water charge had little bearing on the peak pressure response. More important, it appeared desirable to have a minimum charge of water, corresponMng to approximately 80% moisture, to maintain the circulation up to 1000 psi. Other pointo that were omitted vem those that would have the least influence on the program. These ven intermediate points for the pressurized dry well, an intennediate dry well condition, and additional points with small orifice openings. IV-1

M TY-1 1RAN8IENT SEST FAoILTTY 5EST 8CHEDUIZ Point Pressure Inital Break Volume Vent Vent 2 3 2 No. Date nei Moisture Area ft Dry Well ft Area ft Depth ft 6 1 22 1000 .66 .octr86 26.00 2.12 1-1/2" 15 7 1 1000 .66 .ocrr86 17 53 2.121-1/2" 15 8 1 29 1000 .66 .ocrr86 17 53 2.121-1/2" 15 11 1 31 1000 .66 .00177 17 53 9" 15 12 1 30 1000 .66 .01572 17 53 9" 15 13 26 1000 .66 .octr86 17 53 9 "i 75 14 2 1000 .66 .octr86 17 53 9(1") o(15)* 16 2 24 1000 .80 .octr86 26.00 9(1") 15 17 25 1000 .66 .01572 26.00 9" 15 19 24 1000 .66 .00786 26.00 9" .75 20 2 19 1000 .Bo .ocrT86 26.00 9" 0(15)* 24 2 1000 .8o .octr86 20 32 9" 15 9 " /2") 15 25 2 1000 .80 .octr86 17 53 26 2 1000 Kr .So .ocrr86 17 53 9-15 27 32 1 m xe .80 .ocrT86 17 53 9(1-1/2") 15 29 2 11 1000 .66 .ocrr86 17 53 9(1) 1.0 5l')/2") 30 2 27 1000 .Bo .ocrr86 17 53 15 9 1-1 15 31 2 16 600 .80 .ocrr86 17 53 32 3 13 1000 D o .Bo .o1572 17 53 91-1/2") 15 a l 33 3/14 1000 xe .80 .01'572 17 53 9( 1 2") 15 1000 I+EnB.80 .01572 17 53 .25 15 34 1000 MaI .80 .01572 17 53 .25 15 35 Pressurised Dry Well to effect no water in vent pipes. i l f

Additional points were included to detemine the effect of a smaller vent area, the effect of an intemediate depth of submergence, and the effect of vent pipe diameter. We last tests vert run using tracers to evaluate fission product entrainment. These tests consisted of runs with xenon, krypton and heavy water as tracers. C. Description of Test Facility he transient test facility consists in essence of three interconnected pressure vessels that simulate the reactor pressure vessel, reactor containment vessel and the pool containment vessel. A simple schematic arrangement of these volumes for a prototype power plant are shown as volumes (1), (2), and (3), respectively, in Figure I-1. Such an arrangement did not permit the accessibility and flexibility necessary for obtaining test points to fulfill a multi-parameter test program. Sherefore, the test model was arranged as shown in Figure IV-1, where volumes (1), (2), and (3) correspond to the reactor pressure vessel, reactor containment vessel and the pool containment vessel, respectively. A picture of the test installation is shown in Figure IV-2. A brief explanation of the operation of the facility vill facilitate further discussions of the system. Water in the reactor vessel is heated to saturation conditions at high pmssure and then discharged, through an orifice plate into the dry well, by breaking a rupture disc. Part of the water, after it flows through the orifice, flashes to steam. 'the steam-water mixture is then discharged from the dry well, through the vent pipes into the water pool where the steam is condensed. The scale size for the test facility was detemined largely by the size of the pressure vessel used to simulate the reactor vessel. This vessel was in storage at the VBWR site and escentially ready for use. Fortunately, the vessel volume was a factor of one thousand smaller than the proposed 50 Mw reactor vessel. Using this volume factor and the dimensionless scale factors as determined in the analytical model, the area scale factor was 100 to 1 and the linear scale factor was 10 to 1. A time scale of 10 to 1 was accepted, rather than distort physical dimensions to acconnodate the inability to scale intrinsic fluid dynamic properties. Reference Draving: 196 E 929 - Arrangement - Pressure Suppression Test Vessel Instrumentation he primary instrumentation consisted of the pressure transducers and the four channel Sanborn recorder. %e pressure trs'isducers on the pressure vessel, dry well, and the containment voluu were of the strain gage type made by the Statham Co. hey were rated at 1000 pois,100 psia and 15 peig, respectively. The fourth pressure transducer, used to measure IV-2

TRANSIENT PRESSURE INSULATION PT-1 RESISTAllC E TEST FAC/ L /TY '0 PT' PRESSUR E o PRESSURE o 'rNAUSDUCER CH[TURAL " \\, VESSEL-f[TC-l TC = THERMOCOUPLE - N T = THERMOMETER ciRcuL ATion , a VOLUME @ PT-2 7 PT-4 (A P) PT-3 OR IFIC E ( RU PTUREj DISK P 4 c l 4 B LAST / h CAP CONTAINMENT \\\\ TC-6 VESS E L DRY VOL ME VOLUME @ ll : WELL ll y5 SAMPLE TUBE 1 7-6 -VENT PIPES m l POOL i FI G U F '. k'- IV - 1 l .~

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the differential pressun between the dry well and ths contairement volume was a 50 poi reluctance type transducer made by Pace Engineering Co. Excitation voltage for the transducers on the pressure vessel and dry well was supplied by 6 volt batteries. De output signals for these two devices un fed into stabilized D. C. preamplifiers of the Sanborn recotter. De containanet vessel transducer and the differwntial pnssun transducer wre coupled to carrier preamplifiers of the Sanborn neorder. 'Ibe carrier preamplifiers supplied 2400 eps excitation signal for both transducers. De response of the Sanborn recorder is limited to about 100 eps. Se stabilized D. C. preamplifiers have an output Jack with a frequency nsponse of about 10,000 cps. max. De pressure transducers all have natural fnquencies on the order of 10,000 cps or better. An oscilloscope fitted with a camera was used in a few of the early tests to check the nsponse characteristics of the Sanborn recorder. No deviation in response could be detected. A Bourdon tube pressure gage was mounted on the pressure vessel for convenient checking of pressures during the heating period. Temperature for reco241ng test conditions and monitoring during the heating period were measured with chromel-alumel thermocouples and a General Electric potentiometer. Se thermocouples ven numbezwd mod located as follows: 1. Lc:sted in the pressure vessel 8 inches above the face of the 10" flange. 2. Located in the 6 inch discharge tube approximately 6 incht s above the orifice plate. 3 Lccated in the 6" discharge tube approximately 4 inches above the orifice plate. 4. Located with the blasting cap to monitor the cap temperature during the heating period. 5 Located in the dry well approximately 3 inches down from the 24" flange of the dry wil. 6. Locsted in the dry well approximately 32 inches down ft..s the face of the 24" flange of the dry well. 7 Located in the containment volume approximately 12 inches down from the top head on the northeast side. De pool wat4r temperature was measured in some of the latter zuns with an immersion mercury therinometer. Se level of the pool was measured with strips of measuring tape strapped to vent tubes that wre visible through the signt ports. A water manometer was used to determine the prwesure in the dr/ vell for the tests conducted with a pressurized dry well. A conductivity probe was inserted at the discharge erri of a vent tube to determine the instant the IV-3

L water was espelled from the vent tubes. Bis signal was recorded using the enternal timing trace sinuit of the Banborn recorder. Reference Drawing: 218 3 690 - Instrumentation Diagram i f Pressure vessel he sinalated reactor pressure vessel, shown as the insulated vessel in Figure IV-2, was fabricated from 10 inch schedule 80 pipe, flanged on one { end and esyped on the other. the vessel is approximately 70 inches long with a volume of thne subic fbet. Se discharge passage was obtained with a 6 inch pipe welds,4 to a special reduciag-mounting flange to which the 10" flange of the pmssure vessel was bolted. M e 6 inch pipe was fitted with the flanges necessary to hold the orifice plates, rupture discs, the shock tube and thrust balancing impact plate. S e shock tube had two extension pieces for use with the tests having diffennt dry well volumes. i he choice of 6 inches for the discharge and shock tubes was based on hi having as large diameter as practical to prevent excessive bubble fomation i' in the discharge section above the orifice and to aintaine the back pressure on the discharge side of the orifice due to " choking" in the shock tube. Both of these effects are in the direction of reducing the mass flow rate. he physical dimensions of 900 pound class flanges made any sites larger than 6 inches undesirable. A view of the pressure vessel showing the details of the discharge section is pasented in Figure IV-3 The orifice plates were made of 1/2" thick stainless steel with a " sharp edge" of 1/16 inch thickness and a 450 bevel, t ree diameters were made measuring.599 inches,1.199 inches and 1599 inches, respectively, sach of these plates had a dish of approximately 90 mils after the first run i which 414 not appear to become greater. These plates remained in good l condition, with respect to the shart edge, throughout the test program with the exception of those used for the fj ssion product contaissent tests. (Pieces of the glass sample bottles roughened up the upstroom edge durin6 thesetests.) The thrust balance plate at the bottom of the shock tube was designed to l withstand approximately 70,000 pounds of thrust. The support bars won turned to a diameter slightly smaller than the thned roots on the plate end and won welded at the top end only with as imach free length as could I be conveniently obtained to provide "springyness". Over design of the thmst balance system was felt justifiable to assure the pressure vessel would not become a missile. h pressure vessel was fitted with a " christmas tave" on the top or capped and to mount the valves and pressure istmments. Rose consisted of a blow down volve, a safety valve, a pressum transducer, a pressun I gege, and the temperatun bulb for the power controller. In addition, there won bayowt thermocouple fittings located as followst one in the side of the pressure vessel B" above the face cf the 10' flange; smo two located in the 6" discharge tube (k" and 6". respectively, above the face of the 6" flange). A 1/4" pipe drain line was located 8" above the face of the 10" flange. IV-4 i

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As arrer of forest emlrot asA strip weistance heating units som usunted on the asternal surface of the p m ssure vessel. Rose units were held 4 l la place with steel boots and covered by sheet steel with 1-1/2" of 8% magnesia insulation over the sheet steel. An additional en1 rot heating j unit was mounted below the special reducing-mounting flange. 'he lastalled heater espacity totaled 33 5 mt; however, due to aifficulties esperienced l is obtaining fully esturated conditions up to 1000 psi only 14.1 KW of i taput were norus11y used for heating. 21s was obtained with the lower bank l of 2 calrod units and the entrod unit mounted on the special flange, each I rated at 4 7 Kw, 320 volts. i Valform heating of the water was successfully obtained by installing a sheet metal ehleney device inside the pmasure vessel to promote circulation i during the heatias period. his devios consisted of a bottom section k inches o in diameter joinse by a transition section to a top section eight inches in diameter. Se bottom section extended within a few inches of the bottom r (the orifice plate) of the 6 inch discharge tube. Se top section extended j 42 inches into the 10 inch pressum vessel. Se top was ended with a perforated l section and a ring cap to improve the circulation pattern. h is chimney j estended appromientely 12 inches above the lower bank of calrod heating units. Dry Well and Vent System he dry well volume, number (2) of Figure IV-1, was fabricated from a section i of 24 inch pipe joined to a section of 40 inch pipe with a conical transition piece. A quarter top view of this vessel is shown in Figure IV-4 h is unit j was mounted on the containannt tank by means of a 42 inch by 24 inch reducinE i flange. Se 24 inch pipe passed through this flange to allow bolt clearance on the 24 inch flange. Se 24 inch flange was the mounting for the special l reducing-mounting flange of the pressure vessel. Two additional 24 inch j pipe sections of 1 foot and 2 feet, mapectively, were also munted on this flange for inomasing the dry well volume. 1 i De bottom pprtion of the dry well voleue was fabricated with an outsida diameter of 40 inches. Se diameter of this portion was determined largely i by the site of the vent pipe arrangement neeessary to give adegante vent pipe area variation for the test program. Se vent pipes were arranged f to give an annular array of pipes that woald sisadate as amarly as possible that postulated for a prototype power plant using a concentric pool arrangement. Bere von 150 one and one-half inch Almanter pipes arranged in r, has pattern with an inside clearance diameter of 16 isches and an i outside diameter of 39 inches. Nipples were welded into the 1-3/4" thick i } " tube sheet" and fitted with couplings. Se vent pipes used were 11/2" { and 1" in diameter. Reducing bushings vem used with the 1" pipes. De i vent pipes are shown in Figure IV-5. 'this particular armagement shows t 64 1/2 inch pipes lastalled to represent the area obtained with i 150 - 1" pipes. I i l 1 I l IV-5 i .~n--w-w m - v w,m __ p eg+, w,,,, _

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A " water bucket" was installed inside of the dry ven to ntain the water that did not flash to steam during the event and to prevent direct impinge-ment of the water-steam mixture onto the vent tubes. It's questionable if this bucket ever retained much water. Fittings were instaued at var *ous points on the dry well vans to obtain l the pressun and temperature redings in the dry ven volume. Pool and Containment Vessel Win vessel, indicated as volume (3) of Figure IV-1, van a six foot diameter tank having an over-an length c,f 9 feet with dished heads. De top head van fitted vitn a M inch flange that served as the support surface for i the L2 inch naucing flange of the dry ven vessel. %e tank van fitted v with numerous 1-1/2" couplings to facilitate passage for leads to thermo-l couples, pressure transducerc, sample tubes, power cable for interior lights, and other devices. A 3" drain van located at the bottor.. ,i A lif pipe vat instelled in the middle of the tank to sientiate.the pool geometry of a concentric pool. Figure IV-6 is a vectical view looking l into the containmnt tank with the ury well removed. % is view shows the I standpipe, pressure pick up pipe, sample tube, and the tubing with the conductivity probe. %e conductivity probe was used to give a signal when j the water had been expelled from the vent tubes. he timing trace of the Canborn reconier was used for recording the signal. gl l. Wat prueedure j %e general tect procedure followed a logical onler of asser.bly, charging, [ stemnin6 and firing. We pressen vessel was "tr.attoned up" with the J proper orifice plate and rupture disc in the 6" discharge tube. We tupture charge, consisting of an electric blasting cap and several pieces f of prian-coni, vns placed under the rupture disc at Liis time. A theno-( i couple was placed with the blasting cap to sonitor the cap tecperature during the heating period. Most of the tests were mn with water cooling on the caps to prevent pmcature firing. I We noct successful method of rupturing the discs vns obtained using Honel discs that were rated about 30% over the operating pressure with a 603 vee groove cut at about L.5 inchen diameter. We groove depth depended upon the thickness of the disc. S e firing charge was placed l at a point on this gmove and detonated with batteries at the proper tim. If the disc failed to tupture due to either a r.isfim or a weak charge i the depth of the groove vus such that the disc would zvpturti naturally at l a pressure between 1025 and 1075 %e undesirable acpect of the 'apantaneous" type of operation is not knowing the time of rupture. Ein recires the chart to be run at reduced speed to assure a supply of chart I paper when the event doet. "go". ? IV-6 i )

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The pressure vessel was filled with a given charge of water from a calibrated barml. his was accomplished by pulling about 20 inches of vacuum in the pressure vessel and drawing the water in with the vacuum. his procedum demerated the water as it entend the ymssure vessel. An alternata procedum was to fill the prensure vessel completely with water and drain a measund amount off as the pressun built up. he latter procedure was used primarily for the tests with samples for the I entrainment studies. Heat for steaming van supplied by two calrod heating units on the. 4 of the pressure vessel as near the bottom (flanged end) as possible and a single unit on the bottom of the special reducing-mounting flange. Each of these units was rated at 4 7 KW - 220 VAC. he heating period was about l 4 hours, providing the internal circulation continued to 1000 psi. Every l attempt was made to have the heater on the reducing-mounting flange tumed on about one hour before the pasoure vessel was charged with water. During the heating period an asbestos blanket was wrapped around the pressure 6 vensel flange assembly to reduce heat loss at the bottom of the vessel. During the heating period, an other preparations ven made. The condensing pool was iilled to the proper level, cap cooling vater was adjusted, themo-L couple' hooked up and checked out and the pressure transducers calibrated. All of the pressure traneducers were calibrated at least once a week with a dead voight gage tenter. The calibrations were performed on the Sanborn recorder and test values ncorded for convenient checking. Usuany the recorder vsc mn at very low chart speed during the heating period. As l the preneure approached 1000 psi the chart speed was stepped up as a precautionary measure to insure a trace in the event of a premature npture. The chart was usunny run at 25 to 50 minimeters per second for normal firing. All temperaturts were recorded just prior to svpture. he dry veu and containment tecperatures were reconled just after the event. The procedure for running the fission product entrairusent samples van essentian y the same. he tracer samples were inserted in the pressure vessel in the appropriate manner and time. Das and vuter samples were withdrawn for analysis fron the containment vessel and pool. W prevent the samples of xenon and krypton from conecting in the steam dome, the samplen were inserted in the pressure vessel contained in the 250 cc sample bottles with a sman veep hole that would permit balance of pressure during the heating period. A plug of cerro-bend in the discharge tube of the sample bottle prevented loss of gas from the sample prior to the sample being submerged, discharge tube down, in water. We cerm-bend melts at about 160 F to open the discharge tube to the water. When the disc ruptured the prenoure unbalance van sufficiently large to ahatter the sample bottle and release the gas to the discharging water. I r A ^ IV-7

It is intended to use this same technique with elemental iodAne a*a the tracer. he tests using soluble salts and insoluble puticulate matter will be zur, vj+Ja these trscers fne in the water charge. Basqples for analysis are collected in 250 ce two yetewk sample bottles. De bottles won first evacuated anc. the sample drava trit,o them. Where possible, the bottles won purged for a few minutes. Y.ie gas samples were sent to the Consolidated Electrodynamics Corporation for malysis on a mass spectremter. 4 9 5 IV-8 _ _ _ - _ _ _ _ _ _ _ _ _ _ _ - _ _ - _ - _ _ _. - - _ -. - _ - _ - - - _ - - _ -.. - _ _ _, -. _ _ - _ - _ _ ~ _

i i i D. Discussion of Results The test results obtained from the transient test facility are very encouraging. In general, they indicate that the pressure response characteristics of various couponents of the pressure suppression system may be calculated with a reasonable degree of accuracy and conservatism. In addition, the results of tests with tracer materials indicate that the pool does serve as an effective barrier in retaining fission products. Of primary interest were the many test points run to determine the influence of system parameters on the characteristics of the pressure response in the various pressure vessels. Parametric variations were made about a given base condition. The base point conditions were those of runs number 8, 25, 26 and 27 (Figures V C-3, V C-13, V C-14, and V C-15). j L Primary data for the transient tests consisted of the pressure -I response traces obtained from the Sanbo: n recorder. These traces were of transient pressures in the pressure vessel, the dry well, h the containment vessel and the differential pressure between dry [ well and containment vessel. Figures V C-1 through V C-20 are reproductions of these traces. The pressure and time scales have been noted on each trace. The conditions for each test may be obtained from Table IV-1. The usual chart speed was 25 or 50 millimeters (the smallest chart division) per second. There are a few at lower chart speed. These are the traces obtained when malfunction of the firbg system imposed " natural" rupture of j the disc. I In addition to the pressure traces, temperatures were recorded I just prior to and just after the incident. The tenperature summary is given in Table V C-1. Inspection of the temperature data fcr thermocouples No. 2 and 3 will indicate the difficulty experienced in obtaining fully saturated conditions up to 1000 psi. with i natural circulation. After the proper techniques were discovered, a l substantial number of points were obtained with fully saturated conditions in the pressure vessel, i Dry Well Pressure Resoonse Peak pressure in the dry well is the most important single design consideration in a pressure suppression system.- Therefore, the comparisons of test data to calculated results for peak pressure in the dry well provide the primary basis for evaluation of the r calculated results from the analytical model. These cocparisons are shown on Figures IV-7, IV-8, and IV-9. One may immediately I note that all of the test pressures are lower in level than the ( I i ? IV-9

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i corresponding calculated points. However, there is generally good correspondence between calculated and test values for variations in parameters. This correspondence is even better when the effect on peak pressure of subcooled water in the discharge tube has been considered. -This will be discussed later. Another meaningful comparison is that for the elapsed time until peak dry well pressure is attained. Figure IV-10 is a bar graph showing this comparison using the test points for which this value could be obtained. In all cases, the test results indicate longer time intervals than the calculated values. This is in agreement with the lower test peak pressures. An analysis was made to determine if the analytical model could properly account for the effect of subcooled water in the discharge tube. For the test facility, it is primarily the water in the discharge tube that is released during the time interval to reach peak pressure. The energy content of this water is critical with respect to the value of peck pressure. Analytical model results were obtained using the test temperatures of runs 8 and 25 to determine energy conditions in the pressure vessel at the time of rupture. Direct comparisor.s could be made between test values with subcooling and analyticci values with subcooling. The results of this compari-son are shown on Figure IV-11. To accentuate the correlation, both sets of results have been plotted as functions of difference in peak pressure with peak pressure at O'F subcooling test or analytical i as a base. This correlation indicates excellent agreement between test and analytical results for subcooling. It was not possible to treat all points with subcooling in this manner, therefore the graphical correlation shown on Figure TI-12 was devised to determine the correction for subcooling to apply to a given test point. The ordinate for this figure is the peak pressure difference between the analytical model value for a given condition and the corresponding test value. As may be noted, some liberties in generalization were necessary to obtain 4 working data. Figure IV-13 is a comparison of the peak dry well pressures, and the tine interval to reach peak, versus orifice area for corres-ponding test and analytical values. The test values have been corrected for subcooling in the manner of Figure IV-12. This curve clearly shows the increase in deviation between test and calculated values as orifice area is increased. The most plausible explanation for this discrepancy is the reduction of flow per unit area through the orifice as the orifice area is increased. l l IV-10 l

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_ _. ~. 1 Such a reduction in flow per unit area is most probably due to steam bubble fonmation upstream of the orifice. Any steam in the water at the orifice will reduce the mass flow rate out of the pressure vessel. Unfortunately, the. reduced area of the 6" discharge tube probably helps to promote upstream bubble formation. This situation may not be too misrepresentative of a reactor vessel where for any break below the water line there would be baffles or other internal members in the immediate vicinity. There are other possib:e effects that could cause or contribute to the deviations. One of these is choking in the shock tube downstream of the orifice due to the expansion of the released e steam. This effect is easily calculated and is present to the extent that it might reduce the flow by as much as 10% for the large orifice passing theoretical flow rates. Another effect may be the condensa-tion of released steam on the dry well walls. One would expect that condensation ef fects, if present, to be more predominate for small orifice areas with the associated longar time intervals than for larger orifice areas. This effect is not easily calculated for the confused conditions in the dry well during the time interval to peak pressure. Upper limit estimates for tt s effect corresponded to a subcooling of about 10'F. This is eqJivalent to about 2 psi variation in peak pressure which is not very significant. The last effect worthy of consideration is the behavior of the water as it is expelled from the vent pipes. Again, the analysis of the exact physical phenomenon is messy and one might expect that any discrepancies would make the test values high relative to analytical values (for peak pressure). It is possible to obtain a loose correlation (not shown) from the test data that indicates some deviation due to depth of submergence (or behavior of water in the vent tubes). It should be pointed out that the limited number of test points does not permit extensive comparisons of parameter interactions. Returning to Figure IV-13, a simple check to confirm the relationship of peak pressures and time intervals, test relative to calculated, may be made as shown by the lines A, B and C. The value of peak pressure on the test curve may be translated to the calculated curve to give a pseudo-value of orifice area. Using this pseudo-value of orifice area, a corresponding time i'nterval may be obtained on a i. the calculated curve. Within the limits of test accuracy, this value agrees very well with the test value corresponding to the original orifice area. This check lends strength to the argument of reduced flow through the orifice and tends to confirm the j accuracy of the analytical model for predicting peak pressuees and time intervals. 1 IV-ll j i

General Considerations of the pressure Response Characteristics Casual inspection of the pressure response curves (Figures V C-1 to V C-20) reveals several inte.esting phenomena for each of the pressure traces. It should be noted that the traces presented are for the condition of water discharge from the bottom of the pressure vessel. With this condition there is no lingering release of steam after the event since all of the water is expelled from the l pressure vessel. In short, the event is more abrupt and violent l for a given area than would be true for a break releasing steam only. The pressure response of the pressure vessel exhibits extremely interesting behavior. There was an imediate drop in pressure of 50 to 75 psi. in a comparatively short interval (.020 to.040 sec.) followed by a somewhat constant pressure with erratic fluctuation for a period of.3 to.4 seconds. presumably, this is a period in which violent flishing is occc ring to restore equilibrium conditions. Following this is a period during which the pressure decay is relatively gradual indicating that water (with whatever entrained steam is present) is being expelled. After the last of the wcter is expelled, the pressure decay trac ? for the remainder of the event exhibits the exponential decay characteristics of gas expansion within a confined vessel. The effect of discharge diameter variations on the pressure decay characteristics may be evaluated by comparisons made on Figure IV-14 l for the.6,1.2 and 1.6 inch diameter orifice plates, respectively. l l The dry well pressure response traces also offer material for interesting speculation. The most prominant feature of these traces, in general, is the sharp peak pressure that occurs at the instant water is expelled from the vent tubes. For many of the runs, the timing trace was used with the conductivity element to indicate l when the water was expelled from the vent tubes. In all such cases, l the disruption in the sine wave of the timing trace coincided with I the peak pressure in the dry well. See, for example, Figures V C-5, V C-12, V C-16 and V C-20. For most conditions tested the dry well pressure dropped to a low l value immediately following the peak. Occasionally it went negative with respect to the containment pressure with subsequent attenuated oscillations similar to an under-damped spring-mass system. The pressure then leveled off at a few pounds per square inch above the containment pressure for the duration of blow-down of the pressure vessel. Imediately a fter the blow-down period the dry well pressure would drop to a substantial negative value with rather wild fluctuations. This particular behavior was in part anticipated. The steam atmosphere in the dry well and pressure IV-12 1

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vessel condenses on the walls of the dry well and creates a vacuum that is intensified as cold water sprays into the dry well through the vent tubes. There is, however, a puzzling inconsistency in that many of the tests (identical reruns in some cases) did not exhibit any negative pressure in the dry well. One may see the pronounced effect of the pressurized dry will on the peak dry well pressure by comparing the pressure traces of Figures V C-14,and V C-20 with Figures V C-27 and V C-17, I respectively. The test peak pressures were 8 psig compared to 35 psig and 12 psig compared to 25 psig. (No correction has been made for the ef fect of subcooling). The purpose of the pressurized l dry well is to exclude water from the vent pipes. This, of course, i reduces the pressure build up necessary to blow the vents clear j of water. } The trace of dif ferential pressure between the dry well and contain-f' ment volumes indicated essentially the same information as the dry well pressure alone. This pressure gave a convenient measure of I the quasi-steady-state pressure difference between the dry well ) and containment volumes. It is this pressure differential that j forces steam to flow, during the incident, from the dry well into l the pool. ? It is interesting to note that the dry well pressure decay following j the peak differs in characteristics between the runs with the large i orifice and the medium orifice. Figures V C-5 and V C-9, with the l large orifice, show that the dry well pressure tends, as might be 1 expected, to decay exponentially from the peak. The test results j shown in Figures V C-19 and V C-20 do not show this e f fect so I pronounced indicating that the diameter (or length to diameter ratio) l of the individual vent pipes may influence the after-peak pressure response. Runs 12 and 17 were with la vent pipes and runs 32 and 33 were with 1-1/2" vent pipes having an equivalent total area of the 1" pipes. The question of necessary vent area is an important one for economical design. Inspection of any of the dry well pressure traces indicates that there is more vent area than necessary since the pressure following the peak is considerably less than the peak. Run number 30 (Figure V C-17) had about one-half of the vent area l (.5 vs. 9 sq. ft.) of run number 26 (Figure V C-14) with no observable change in peak pressure and only a slight ir. crease in the a f ter-peak pressure. Presumably the vent area could be minimized to the point where the i pressure following the peak would be very close to the peak. Fer j the conditions of the runs cited above, this would mean the vent f area could be.1 square feet or so with no increase in dry well l peak pressure. j 1

The pressure response of the containment vessel is quite interesting in that a peak pressure of 1.8 to 2 tiews the quasi-steady-state pressure occurs just after the drop-off in peak dry well pressure. This behavior can be explained by assuming that the air in the containment vessel is compressed adiabatically by the injection of a major portion of the dry well air into the containment vessel. And this process is followed very quickly by an evaporative cooling process due to the water thrown around within the vessel. Calculated values for such a sequence of events agree fairly well with measured values. For example, for run No. 30 (Figure V C-18) the peak was calculated at 7.2 psi versus 7 psi measured and the quasi-steady-state value as 4.6 psi. compared to 3.8 psi, test. The pressure traces indicate that the air is expelled from the dry well throughout tne event. The continual rise in containment pressure until the second peak is reached provides the basis for this conclusior. The measured temperature rise of the pool agreed generally with l calculated values. The pool temperature rise was calculated as 0 0 0 7.5 and the measured values were 10 and 7 for runs 32 and 33, respectively. A most important observation of the pressure behavior for the entire system is that all of the individual volumes return to essentially atmospheric pressure immediately following the event. This should be significant in containment leakage considerations. Fissien Product Entrainment Tests The results of the noble gas fission product entrainment tests are encouraging but not particularly conclusive with respect to numerical values for effectiveness. Two tests were run with a 250 cc. (standard conditions) sample of xenon and one test was run with the same size sample of krypton. The amount of xenon in a 50 MW (electrical) reactor was estimated to be about 203 gm. The test sample had about 1.2 gm. Scaling the test sample by the volume scale factor of 1000 indicates the test concentration to be 6 tines that of the reactor, if all of the gas in the reactor is released! For all three tests the entire sample bottle was suspended inside of the pressure vessel in such a manner that the gas would be trapped in the sample bottle until the event was I initiated. Thir was accomplished with a weep hole (20 mills or so in diameter) that would accommodate slow changes in pressure. A rapid change in pressure would cause the sample bottle to explode releasing the gas into the discharging water. IV-14 I

'w-m-.=.

The first test using xenon (run 27) and the test using krypton (run 26) appeared to perform in the desired manner. The second run with xenon did not have the gas sample released as anticipated. The weep hole was unintentionally too large (approx. 25 inches [ diameter) and the sample bottle did not rupture. For this run, r most of the gas was probably released during the last half of the l event. At the conclusion of the incident, gas samples were obtained from f the pool space and sent to Consolidated Electrodynamics Inc. for i analysis on the mass spectrometer. Their analyses were as follows : l Mol percent l f. Air + CO X'" K#VDt " 2 Krypton sample 99.997 .003 + 100% i - 50% I Xenon sample #1 100.00 0 I w Xenon sample #2 100.00 0 1 If xenon was present it was less than.005 mol percent which means f t the amount of xenon gas in the sample was of the order of their I normal instrument sensitivity or less. The sensitivity for detecting i krypton is better because of its unique peaking characteristics. ? I A rough accountability of the krypton test indicates that the water pool could be supersaturated with krypton by a factor of 5 to 20. l The variation is based on the accuracy limits of the analysis. I The results of the tracer tests using heavy water have not been I received at the time of writing the report and nothing can be said regarding this test. E. Conclusions The results of the transient test facility have provided conclusive evidence that the pressure suppression system of reactor containment is ef fective in containing the energy released from a boiling water reactor incident. Furthermore, the pressure behavior of such a system may be calculated with a reasonable degree of accuracy, and these values are conservative when compared to the test values. The primary ef fect that contributes to deviation between calculated values and test values appears to be the nature (or state) of the j flow out of the pressure vessel. The analytical model assumes the flow is entirely saturated liquid. For the model tests, there is no practical methed of determining the state of the fluid at the orifice during the fraction of a second before peak pressure is reached. One must conclude from analysis of the test data the l degree of choking present and consider the deviation caused by g l choking as design margin if necessary.

There are three primary parameters that determine the peak dry well pressure. These are the break area, the depth of submergence of the vents, and the dry well volume. Of these, the depth of submergence is the easiest to control by design and various " tricks" may be used to reduce the effective depth of submergence. One of these tricks used in the tests was to pressurize the dry well to force the water from the vent pipes. This wt s extremely ef fective in reducing the peak dry well pressure. The gain doesn't come " free", however, as the additional air expelled from the dry well increases the containment volume pressure. Other characteristics of the dry well pressure response indicate several points of interest. The vent area that must be provided is directly a function of the size break that must be considered. The depth of submergence, for a given break area, is the prime determinant of what value the peak pressure will have and the vent area may be varied over a wide range with little influence on this pressure. There is, of course, a minimum value of vent area that will produce a sustained (for the duration of the event) pressure equal to the nominal peak value. However, such a vent area would produce a higher peak than a larger vent area would produce for a more serious break. The test results suggest that the vent area could be reduced by a factor of 3 or 4 with no increase in peak dry well pressure for the conditions tested. Dry well vessel designs must give due consideration to negative pressures in the dry well. For the case of a rupture in the bottom of the pressure vessel, all post accident steam generating capacity is lost by dumping the reactor water into the dry well. When the event " tails out", steam in the dry well begins to condense with an associated reduction in pressure. Cold water is sucked in through to vent pipes to promote further condensation. Measured dry well pressures went as low as -12 psi. Such behavior would prohibit the normal blowing of safety valves directly into the dry well. But such behavior could be utilized to air in flooding the dry well after an accident. The design of tue containment volume must be based on the peak l pressure anticipated in this vessel. The nature of the pressure response for this volume indicated adiabatic compression of the air in the containment volume by expulsion of air from the dry well. There was a peak pressure followed by an evaporation cooling process with the pressure dropping considerably and then a gradual rise in pressure to an intermediate value during the event. A prototype would probably not have as violent pool action as the model and less evaporative cooling. It is very significant that the entire system reverts back to essentially atmospheric pressure after the incident. This is an important consideration for fission product leakage. The fission product entrainment tests to date indicate that the pool is effective for retaining noble gases. l

1 i I SECTION y, APPENDIX QI92L A Condensing Test Sample Data and Detailed Program l B Condensing Test Methods of Analysis C Transient Test Data D Transient Test Methods of Analysis E Reference Drawings h O i l l

FIG. V-A-1 8" VERTICAL INJECTOR - ANCHORED CLOSED TANK COLD POOL WATER 6' DEPTH OF SUBMERGENCE VIRTICAL SCALE-2 PSI / DIVISION HORIZONTAL SCALE: 10 MILLISECONDS' INCH RUN 1 MASS FLOW RATE 85,800 #,HR. MASS FLOL' KATE 69,'l00 f, HR. l l )' t a .] y \\ w.., w -- 4 4 1 s -<ie- ~ I 1 i I j l i 7. .g q l w-9 si = .i

c. -

- 1 ,( ii. 1 1 !%ES FLC'.? RATE 81.'l00 # HR. MASS FLOR RATE 56.'/00 g HR. I%23 FLOC EATE 1.2.300 #fHR. W.SS FL0k' RATE 114.65) ri :-3. ._} l_ ,I .i ,I m C - a>----- p 4 J. i -1 i. I -l I 6; e 1 i . l . i i ti w. j n;%$ 4 a e. =- < 9 ms -s L 'j' q 1 l 1 k -g g .] .;c m. j u t s o r t* TTM' Com? M 1% J.* /*--

d FIG. V-A-2 l \\ 8 VERTICAL INJECTG - ANCHTED { CLOSED TANK COLD TO HOT POOL WATER 6' DEPTH 07 SUE G GENCE VDITICAL SOALE: 2 PSI / DIVISION H@IZONTAL SOALE: 10 MILLISEOC!OS !!CH RUN 2 O 0 POOL TEMPERATEE BO F POOL TD!PERATURE 103 F 1 t 9 1 j l> j l j' - - 1 4 y I t l ] ,i j ~ i .M l ~^ \\ + ~l l~- l l ~~ POOL TEMPERATb.lE 90 F POOL TD'PERATURE 110 F POOL TDPERATURE 115 F j i1 j i ~ l W. ] )]

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FIG. V-A-3 3" VERTICAL INJECTG1 - ANCHORL'D CLOSED TANK .90I POOL WATER 6' DEPTH OF SUBMERGENCE /ERTICAL SCALE: 2 PSI / DIVISION HORIZO?TIAL SCALE: 10 MILLISECO!OS/ INCH RUN 3 4 ASS FLN RATE 90,003 #fHR. MASS FLW RATE 68,200 #/HR. s l o s - w_. i g es-- - l l~ = i q ] r., i ~I lll .,j l ,;.i MASS FLOL' RATE 79,003f/HR. P. ASS FLU' RATE 55,000 it,ER. MASS FLN RATE kl,333 #/ER. MSS FL3: RATE 13,0 >0 a, h?.. k a i f. j w w ~ W ^ w -.. y )I l l~

4 I

l 1 j ,c l ) o . ') hi . 4 s T8 g, ,s 'g p s r k-a s p. "3 e'

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1- { '

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FIG. V-A-5 8'VERTICALINJECTOR-UNANEHORED l l CZ,OSED TANK COID POOL WATER 6' DEPTH OF SUBMERGENCE VEPTICAL SCA E: 2 PSI / DIVISION H N IZONTAL SCALE: 10 MILLISECONDS /INOH RUN 1 MASS FLOL' RATE 81,900 f/s. MSS FLOW RATE 69,800 #/E. l I i - 1 y - n_. 1 g._ _j. ~ 'l. 1. - l;,il:,,;l j 4 4 -1, l-t .4 M ~ gy' a .y l h Ii i 3: l y' I ~ - -,I..- + 7,; i , III llll lili i ) MASS FL0i RATE 32,5005,E. MASS FLOi RATE 56,600s.lm. MASS FLO: RATE L3,300ffs. MASS FLOR RATE 14,'l00t, s. l ' f_ l A 1 ~ - .g } 3 2 i .j ( ~~ Y i 4 + j } j 1 l l_ di. l q 4 ~ v 'q i e l J .p. g,- y 0

a l

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j 1

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s I

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FIG. V-A-7 8" VERTICAL INJECTOR - UNANCHORED i ~ CLOSED TANK HOT POOL WATER 6' DEPTH OF SUBMERGD:CE VERTICAL SOALE-2 PSI / DIVISION HORIZOUTAL SOALE: 10 MILLI 3800:33, INCE JASS FLO.' RATE 83,100 # / HR. FASS FLOL' RATE 67,800 m HP. I I-l i. +- 4 lll {fj!' '81.!{.'.I ~~ l 4 {]1- { y. 3 ~ - - - < n _K d 1 . - / ~ s 4 f ~ n 1 lllllli' 'IIlllll' 1' ASS FLS: RATE 61,700 ?,HR. PASS FLG.' RATE 56,303 ' MR. 1/ ASS FLO.' RATE h2,203 #fHR. FASS FLG: RATE 11+,403 a. < H:. l_ 'l,_ e------ l W W-dg l ~ 2 e Ie n m. e 1, ;- J ~ 4 _ 4 I d' W i _ *3 l i 2 ) 7..;p l y -- ' y * % 8 ' _' t _Y. g-1 s. V, , t. ~ e g ; < l n

\\ FIG. V-A-8 i 8" VERTICAL INJECTOR - UNANCHORED a l f CLOSED TANK HOI POOL WATER k' DEPIH OF SUBIGlGDCE r 4 l VERTICAL CCALE: 2 PSI / DIVISION HORIZONTAL SOALE: 10 MILLISECONDS / INCH 1 s Rtm b PASS FLOh* RATE 85,k00 #/HR. P k-b l-a ) l L'.. I!'i ;!i' A I l.. I I i i ~ ~ ~ _ +L. I illl, . + ~ ll 3 25 FLUi RATE 73,300 4 HR. MASS FLOL' RATE 87,233 */ E. l RW 5 1 2' DEFIH OF SUBIGlGENCE I I (< +-J I,.. g I o------- .n ,.s +- l + uw t .. fi e i s i i J %' l' I. ~ mss rm u:E a,02 o s. t I

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r k T.ABLE. Y. A::1. CONDENSING IEEI, FACILITY DETAILED I12I. PROGRAM Group I 4" Diameter Single Vertical Injector Depth of Run No. Flow Rate Submeroence 1 14,200lbs/hr 6 inches 2 44,500lbs/hr 1 foot 3 51,100lbs/hr 2 feet 4 53,300lbs/hr 2 feet 8" Diameter Single Vertical Injector 1 70,000lbs/hr 1 foot 2 83,500 lbs/'.3 2 feet 3 84,000lbs/hr 2 feet 4 100,000lbs/hr 4 feet 5 100,000lbs/hr 4 feet Group II 3/4" Diameter Orifice 1 200lbs/hr Sealed Tank 2 320 lbs/hr Sealed Tank = 3 390 lbs r Sealed Tank 4 470 lbs r Sealed Tank V A-14

Group III a. 6" Diameter Single Vertical Injector Depth of Run No. Flow Rate Submeroence 1 48,400lbs/hr 6 inches l 1a 83,300 lbs/hr 6 inches 2 22,500lbs/hr 6 inches Sealed Tank 3 44,000lbs/hr 6 inches Sealed Tank 4 64,200lbs/hr 6 inches Sealed Tank 5 83,300lbs/hr 6 incher Sealed Tank b. 6" Diameter Single Vertical Injector 1 35,600lbs/hr 6 inches 46,300 lbs/hr 6 inches 55,000lbs/hr 6 inches 62,200lbs/hr 6 inches 75,000lbs/hr 6 inches 2 67,900lbs/hr 6 inches 86,607lbs/hr 6 inches 3 89,903lbs/hr 6 inches c. 4" Diameter Single Vertical Injector 1 15,200lbs/hr 6 inches 2 51,500lbs/hr 6 inches 3 53,000lbs/hr 6 inches 4 58,000lbs/hr 6 inches Sealed Tank d. 14" Diameter Single Vertical Injector 1 84,400 lbs/hr 6 inches 2 86,700 lbs/hr 6 inches Sealed Tank e. 4" Diameter Multiple Vertical Injector 1 46,900lbs/hr 6 inches 2 90,700 lbs/hr 6 inches 3 52,800lbs/hr 6 inches Sealed Tank 4 66,100lbs/hr 6 feet Sealed Tank i V A-15

Group III (Continued) f. 8" Diameter Single Vertical Injector Depth of Run No. Flow Rate Submeroence 1 78,500 lbs r 6 inches 2 77,500 lbs r 6 inches to 1 inch 3 89,400 lbs r 6 inches Sealed Tank 4 86,400 lbs r 6 feet Sealed Tank g. Top 4" Diameter Horizontal Injector la 24,300 lbs/hr 6 inches 1 55,100lbs/hr 6 inches 2 57,400 lbs r 6 inches Sealed Tank 3 57,400 lbs r 6 feet Sealed Tank h. 4" Diameter Bottom Horizontal Injector 1 60,000 lbs/hr 6 inches 2 61,500lbs/hr 6 inches Sealed Tank 3 63,300 lbs/hr 6 feet Sealed Tank i. 6" Diameter Bottet Horizontal Injector 1 86,400lbs/hr 6 inches 2 89,800lbs/hr 6 inches Sealed Tank 3 97,500 lbs/hr 6 feet Saal Tank j. 8" Diameter Bottom Horizontal Injector j t 1 82,900lbs/hr 6 inches 2 E2,900 lbs/hr 6 inches Sealed Tank k. 14" Diameter Bottom Horizontal Injector 1 83,000lbs/hr 6 inches ( V A-16

Group Ty, 4" Diameter Single Vertical Injector Anchored to Tank Wall a. Depth of Run No. Flow Rate Submeroence Water 1 57,100lbs/hr 6 feet Cold (50 F) Sealed Tank 42,200lbs/hr 6 feet Cold (50 F) Scaled Tank 0 0 14,300lbs/hr 6 feet Cold (50 F) Sealed Tank Cold to Hot (50 -120,F) Sealed Tank 0 2 55,400lbs/hr 6 feet 3 54,500lbs/hr 6 feet Hot (150 F) Sealed Tank 0 41,100lbs/hr 6 feet Hot (150 F) Sealed Tank 28,700lbs/hr 6 feet Hot (150 F) Sealed Tant. 14,800lbs/hr 6 feet Hot (1500F) Sealed Tank b. 4" Diameter Single Vertical Injector Unanchored 1 59,000 lbs r 6 feet Cold Sealed Tank 43,800 lbs r 6 feet Cold Sealed Tank 29,200lbs/hr 6 feet Cold Sealed Tank 14,600lbs/hr 6 feet Cold Sealed Tank 2 57,500lbs/hr 6 feet Cold to Hot Scaled Tank 3 56,300 lbs/hr 6 feet Hot Sealed Tank 43,200lbs/hr 6 feet Hot Sealed Tank 28,600lbs/hr 6 feet Hot Sealed Tank 14,300lbs/hr 6 feet Hot Sealed Tank 6" Diameter Single Vertical injector Anchored to Tank wall c. 1 86,700 lbs/hr 6 feet Cold Sealed Tan 79,900 lbs/hr 6 feet Cold Sealed Tank 68,200lbs/hr 6 feet Cold Sealed Tank 57,200 lbs/hr 6 feet Cold Sealed Ten; 41,800lbs/hr 6 feet Cold Se.ed Tank 29,500 lbs/hr 6 feet Cold Sealed Tant 14,800lbs/hr 6 feet Cold Sealed Tank 2 91,600lbs/hr 6 feet Cold to Hot Sealed Tant

l Group IV (Continued) d. 6" Diameter Single Vertical Injector Anchored to Tank Wall Depth of W l M Run No. Flow Rate Submercance 1 86,100 lbs/hr 6 feet Cold Sealec Tank ~ B3,000lbs/hr 6 feet Cold Sealed 1:nk 71,500 lbs/hr 6 feet Cold Sealed Tank $7,200 lbs/hr 6 feet Cold Sealed Tank 43,800 lbs/hr 6 feet Cold Sealed Tank 29,400 lbs/hr 6 feet Cold Sealed Tank 14,300 lbs/hr 6 feet Cnid Sealed Tank 2 %,300 lbs/hr 6 feet Cold to Hot Sealed Tank 3 90,000lbs/hr 6 feet Hot Sealed Tank 82,400 lbs/hr 6 feet Hot Sealed Tank 68,200 lbs/hr 6 feet Hot Sealed Tank 55,800 lbs/hr 6 feet Hot Sealed Tank 43,300lbs/hr 6 feet Hot Sealed Tank l 28,600 lbs/hr 6 feet Hot Sealed Tank l( 14,100 lbs/hr 6 feet Hot Sealed Tank 4 86,500 lbs/hr 4 feet Hot Sealed Tank 69,700 lbs/hr 4 feet Hot Sealed Tank 5 88,000 lbs/hr 2 feet Hot Sealed Tank 70,7'O lbs/hr 2 feet Hot Sealed Tank 6" Diameter Single Vertical Injector Unanchored e. 1 85,800 lbs/hr 6 feet Cold Sealed Tank 81,700 lbs/hr 6 feet Cold Sealed Tank 69,700 lbs/hr 6 feet Cold Sealed Tank $6,700 lbs/hr 6 feet Cold Sealed Tank 42,300lbs/hr 6 feet Cold Sealed Tank 29,100 lbs/hr 6 feet Cold Sealed Tank 14,600 lbs/hr 6 feet Cold Sealed Tank l. 2 91,800 lbs/hr 6 feet Cold to Hot Sealed Tank 3 90,000lbs/hr 6 feet Hot Sealed Tank 79,200 lbs/hr 6 feet Hot Sealed Tank 68,200 lbs/hr 6 feet Hot Sealed Tank 55,000 lbs/hr 6 feet Hot Sealed Tank 41,300 lbs/hr 6 feet Not Sealed Tank 27,600lbs/hr 6 feet Hot Sealed Tank 13,800 lbs/hr 6 feet Hot Sealed Tank 4 85,000 lbs/hr 4 feet Hot Sealed Tank 68,200 lbs/hr 4 feet Hot Sealed Tank ( 5 85,000 lbs/hr 2 feet Hot Sealed Tank 68,200 lbs/hr 2 feet Hot Sealed Tank u -v:

O Group IV (Continued) i f. 8" Diameter Single Vertical Injector Anchored to Tank Wall ~ Depth of R r A Flow Rate Submeroence ggt,,1 1 1 81,900lbs/hr 6 feet Cold Sealed"Iank 82,500 lbs/hr 6 feet Cold Sealed Tank 69,800 lbs/hr 6 feet Cold Sealed Tank 56,600lbs/hr 6 feet Cold Sealed Tank 43,300 lbs/hr 6 feet Cold Sealed Tank 28,800lbs/hr 6 fe" cold Sealed Tank 14,700 lbs/hr 6f Cold Sealed Tank 2 82,500 lbs/hr 6f Cold to riot Sealed Tank 3 83,100lbs/hr 6 feet Hot Sealed Tank 81,700 lbs/hr 6 feet Hot Sealed Tank 67,800lbs/hr 6 feet Hot Sealed Tank b6,300 lbs/hr 6 feet Hot Sealed Tank 42,200lbs/hr 6 feet Hot Sealed Tank 28,700 lbs/hr 6 feet Hot Sealed Tank 14,400lbs/hr 6 feet Hot Sealed Tank 4 85,400 lbs/hr 4 feet Hot Sealed Tank 70,300 lbs/hr 4 feet Hot Sealed Tank 5 87,200lbs/hr 2 feet Hot Sealed Tank 72,000lbs/hr 2 feet Hot Sealed Tank 9 8" Diameter Single Vertical Injector Unanchored 1 88,800lbs/hr 6 feet Cold Sealed Tank 83,000lbs/hr 6 feet Cold Sealed Tank 70,000lbs/hr 6 feet Cold Sealed Tank 56,200lbs/hr 6 feet Cold Sealed Tank 42,800lbs/hr 6 feet Celd Sealed Tank 28,800 lbs/hr 6 feet Cold Sealed Tank 14,500 lbs/hr 6 feet Cold Sealed Tank 2 88,. 00 lbs/hr 6 feet Cold to Hot Sealed Tank 3 89,900lbs/hr 6 feet Het Sealed Tank 62,000 lbs/hr 6 feet Het Sealed Tank 69,800lbs/br 6 feet Het Scaled Tank 56,200lbs/hr 6 feet Het Sealed Tank 43,500 lbs/hr 6 feet Het Sealed Tank 29,000lbs/hr 6 feet Het Sealed Tank 14,500 lbs/nr 6 feet Hot Sealed Tank 4 88,400lbs/nr 4 feet Het Sealed Tank 70,200 lbs/nr 4 feet Het Sealed Tank 5 88,003lbs/nr 2 feet Hot Sealed Tank 70,200lbs/hr 2 feet Hot Sealed Tank U 21C

Group IV (Continued) h. 4" Diameter Multiple Vertical Injector Anchered to Overhead I-Beam Depth of Run No. Flow Rate Submeroence Water 1 92,500 lbs/hr 6 feet Cold Sealed Tank 84,200lbs/hr 6 feet Cold Sealed Tank 73,500lbs/hr 6 feet Cold Sealed Tor.k 56,100 lbs/hr 6 feet Cold Sealed Tank 42,100 lbs/hr 6 feet Cold Sealed Tank 29,400 lbs/hr 6 feet Cold Sealed Tank 14,400lbs/hr 6 feet Cold Sealed Tank 2 91,800lbs/hr 6 feet Cold to Hot Sealed Tank 3 92,800 lbs/hr 6 feet Hot Sealed Tank 83,700lbs/hr 6 feet Hot Sealed Tank 71,300lbs/hr 6 feet Hot Sealed Tank 58,800lbs/hr 6 feet Hot Saaled Tank 44,100 lbs/hr 6 feet Hot Sealed Tank 29,500 lbs/hr 6 feet Hot Sealed Tank 15,300 lbs/hr 6 feet Hot Sealed Tank 4 92,700_ lbs/hr 4 feet Hot Sealed Tank 69,700 lbs/hr 4 feet Hot Sealed Tank 5 92,000lbs/hr 2 feet Hot Sealed Tank 66,600lbs/hr 2 feet Hot Sealed Tank Group V a. 4" Diameter Multiple Vertical Injector - Tandem Compartrnent : 18" wide x 12' long x 12' deep Depth of Run No. Flow Rate Subrtercence 1 19,050lbs/hr 6 feet 2 28,000lbs/hr 6 feet 3 36,400 lbs/hr 6 feet 4 44,600lbs/hr 6 feet 5 51,400lbs/hr 6 feet 1 61,400lbs/hr 6 feet 2 65,500lbs/hr 6 feet 3 74,500lbs/hr 6 feet ( 4 85,200 lbs/hr 6 feet V A-20

l Grouc V (Continued) comoartnent: 18" wide x 10' long x 12' deep Depth of Run No. Flow Rate Submeroence 5 44,800lbs/hr 6 feet i o 6 52,000lbs/hr 6 feet 7 60,100 lbs/hr 6 feet 8 66,800lbs/hr 6 feet 9 67,200 lbs/hr 6 feet 10 72,500 lbs/hr 6 feet 11 79,200 lbs/hr 6 feet Comoartment: 18" wide x 2' long x 12' deep 12 '28,200 lbs/hr 6 feet 13 37,200lbs/hr 6 feet 14 46,000lbs/hr 6 feet 15 75,000lbs/hr 6 feet 16 52,000lbs/hr 6 feet Comoartment: 18" wide x 8' long x 12' deep 17 40,503lbs/hr 6 feet 18 48,000 lbs/hr 6 feet 19 59,803 lbs/hr 6 feet 20 65,930 lbs/hr 6 feet 21 73,500lbs/hr 6 feet Compartment : 18" wide x 8' long x 10' deep 22 47,900 lbs/hr 6 feet l 23 67,103lbs/hr 6 feet 24 81,700 lbs/hr 6 feet Compartment : 18" wide x 12' long x 10' deep 25 34,700 lbs/hr 6 feet 26 48,503lbs/hr 6 feet 27 70,200lbs/hr 6 feet i Compartaent: 18" wide x 12' long x 8' deep 28 33,703 lbs/hr 6 feet ] 29 48,233 lbs/hr 6 feet 30 68,400lbs/hr 6 feet

Group V (Continued) Comoartment: 18" wide x 8' long x 8' deep Depth of Run No. Flow Rate Submeroence 31 37,000 lbs/hr 6 feet 32 53,200 lbs/hr 6 feet 33 72,500 lbs/hr 6 feet Comoa rtment : 6' wide x 12' long x 12' deep 34 19,100 lbs r 6 feet 35 19,100 lbs r 6 feet 36 36,800 lbs/hr 6 feet 37 54,000lbs/hr 6 feet Compartment: 6" wide x 8' long x 12' deep 38 19,200 lbs/hr 6 feet 39 37,200 lbs/hr 6 feet 40 52,500 lbs/hr 6 feet Compartment: 6" wide x 8' long x 8' deep 41 19,050 lbs/hr 6 feet 42 b. 4" Diameter MJ1tiple Vertical Injector - Side-by-Side Compartment: 18" wide x 12' long x 12' deep 43 19,100 lbs/hr 6 feet 36,800 lbs/hr 6 feet 44 45 52,600 lbs/hr 6 feet Compartment : 18" wide x 8' long x 12' deep 46 19,000 lbs/hr 6 feet 47 36,600 lbs/hr 6 feet 48 52,600 lbs/hr 6 feet Co oartment: 18" wide x 12' long x 8' deep 49 19,000 lbs/hr 6 feet 50 36,800 lbs/hr 6 feet $1 52,500 lbs/hr 6 feet

Group V (Continued) Comoartment: 18" wide x 8' long x 8' deep Depth of Run No. F1mv Rate Subceroence 52 19,000 lbs/hr 6 feet 53 36,800 lbs/hr 6 feet 54 51,900 lbs/hr 6 feet c. 4" Diameter Multiple Vertical Injector - Tandem comoartment : 6' wide x 12' long x 12' deep 55 19,500 lbs/hr 6 feet 56 27,900 lbs/hr 6 feet 57 36,800 lbs/hr 6 feet 58 44,900 lbs/hr 6 feet 59 52,000 lbs/hr 6 feet Compartment : 6" wide x 6' long x 12' deep 60 19,500 lbs r 6 feet 61 28,200 lbs r 6 feet 62 36,800 lbs r 6 feet 63 45,000 lbs/hr 6 feet 64 52,500 lbs/hr 6 feet Compartment : 6" wide x 12' long x 8' deep ~ 65 19,200 lbs/hr 6 feet 66 28,300 lbs/hr 6 feet 67 36,800 lbs/hr 6 feet 68 45,300 lbs/hr 6 feet Compartment : 6" wide x 8' long x 8' deep 69 19,100 lbs r 6 feet 70 27,900 lbs r 6 feet 71 37,100 lbs/hr 6 feet l 72 45,300 lbs/hr 6 feet i V A-23

Group V (Continued) l d. 4" Diameter Multiple Vertical Injector - Tandem Header End of Conpartment to First Injector. 3' Compartment: 6" wide x 12' long x 12' deep Depth of Run No. How Rate Submeroence 73 19,100 lbs/hr 6 feet 74 36,800 lbs/hr 6 feet 75 53,200lbs/hr 6 feet 76 Check surface reaction during expulsion of air from injectors. 77 Check surface reaction duririg expulsion of air from injectors. e. 8" Diameter Single Vertical Injector End of Compartment to Injectors Centerline - 8" Comoartment: 12" wide x 8' long x 8' deep 78 19,100 lbs/hr 4 feet 79 33,000lbs/hr 4 feet 80 53,200lbs/hr 4 feet Compartment : 12" wide x 12' long x 12' deep 81 19,100lbs/hr 6 feet 81a 19,100lbs/hr 6 feet 82 37,200lbs/hr 6 feet 83 54,800 lbs/hr 6 feet f. 4" Diameter Single Vertical Injector End of Compartment to Injectors Centerline - B" Compartment: 6" wide x 6' long x 6' deep 84 3 feet 85 4,000lbs/hr 3 feet 86 11,700lbs/hr 3 ffet 87 21,000 lbs/hr 3 feet Compartment: 6" wide x 12' long x 12' deep BS 6 feet 89 6 feet 90 10,800lbs/hr 6 feet 91 18,500lbs/hr 6 feet i

V-B-1 V-B. CWDENSING TEST METHODS OF ANALYSIS Correction of the Mass Flow Rate Indicated by Barton Flow Meter: hy indicated mass rate Let = h, e corrected mas, rate ~ specific volume of steam upstream of the water, vg = under rated conditions. specific volume upstream under test conditions. V = yg = expansion factor under rated conditions. expansion factor under test conditions. V =

Then, E'

M7 (1) i Y [*1 = Wr The ratioM: Vis assumed equal to unity. The rated conditions upstream l l are saturated steam at 100 psig. Equation (1) reduces to - hr he = 4 Velocity at Iniector Exit : 1. From continuity considerations, the velocity in the injector at exit is l W (3) 4's = g g, The density

m3 is unknown. Either two thermodynamic coordinates must be measured at the injector exit 3 or one coordinate must be h

measured and some assugtion must be made concerning the process which the steam undergoes while flowing through the injector. See end of Appendix V-D for definition j of symbols not defined here.

.-V-B-2 For this series of tests there was no satisfactory way of measuring i other than static pressure at the injector exit. Therefore an i assusption was made (and subsequently, calculations were made to justify it, for the single 4 inch injector at one flow condition) concerning the process in the injector. It was assumed that the flow is isentropic but irreversible. In other words, the heat transferred through the injector wall is just equal to the energy dissipated in friction. The following calculations are made in support of the above assumption. Let F be the rate of onesgy dissipation due to friction and Q the rate of heat transfer. These are given respectively by F = 'D AA t') 23 3 and Q = A UsT (b) The following are reasonable, or typical and consistent, values for the single 4 inch injector, N O = p, S Rs = 700 /.sec D AU=o.4.bs k= 3 y_,,c s r = vo, Substituting in (2) and (3), F = 3+ "h/.sec "N.sec / Q=34 1 is v.sidered good enough agreement to to justify the assumption (evi h.tr.ch at lower flows the agreement would be much poorer than indicated here). If the same friction factor and heat transfer coefficient are applied to some other size of injector the agreement is just as good. ..-__-,..---.-..e.,.

V-B-3 Based on the assunption of isentropic but irreversible flow, and treating the steam as a perfect gas, the following relationship holds : L 5_ R Y ( 0.) ' (s} s, a e-This is good whether the flow is subsonic or sonic. The only difference is that sonic flow has the possibility of being underexpanded, that is, the pressure just inside the injector at exit may be greater than the pressure in the pool at exit. Momentum Rate at Iniector Exit : Momentum rate is given simply by M =- - N (7) as g Mass Flow Rate Measurement with the Sinole 4 Inch Inieetor The following is based on the assumption of isentropic but irrevevsible flow ( Q' : E' ), and treats the steam as a perfect gas. From energy considerations ,l + y, [R7; - R7^] + q ' = 0 Y (e) l From force considerations 2 3 vdp+f'=0 {9) + Note that for isentropic flow the middle terms of the above two equations are equal, confirming that g' and r'must be equal. l l f ~ -... ~

V-B-4 The energy per unit mass F' dissipated by friction is /~'= (10) D 2.9 Substituting in the energy equation ] = l [RE -R71] /+ (11) Consider for the moment the case of sonic velocity. For this special case - uf _ YR7; gg2; ~ 29 2 Combining (11) and (12) y_ j [h - /] (13) /* = Because the process is isentropic 1-1 = (14) Combining (13) and (14) and rearranging, 1*- / [ Ps ) 7 (15) ~- L)

2. J

~ (Note that for reversible isentropic flow this reduces to zero) It was found that in the case of the sinzle 4 inch injector there was a certain critical mass rate beyond which the pressure ratio f/p3 did not increase' This critical ratio is 2.1. Deducing that this (value of '/p, ) coincided with the condition of sonic velocity at injector exit, it was substituted in (15). The corresponding value l of f%was calculated to be 0.24 (It was subsequently found that e.7 ( gave better agreement with the mass rate as indicated by the Barton Flow Meter. The latter value was used in determining mass flow rate with the single 4 inch injector.) l

V-B-5 Now consider the more general case again. Combining (11) and (14) and rearranging, Vf = y j f/ ~ ) (16) Substiting 9 forp,-A, and expanding the second term on the right of (16), U$ = / fiI' f + fy*$ f)+ ----] (17) ~ From continuity As Ms 4'3 (18) = Because the process from 1 to 3 is isentropic, uls = ul {p 4); (I ~ f) (19) = i Expanding, ~ ~ 3 2 (20) ~~ Combining (17), (18), and (20), the mass rate is given by Y = A3f-ffg A f] f /' 4 y f - ' f' 'pA5 $21) Note : If errors of less than 10% are permitted, then for T= 1.3 and for all Vp, less than 0.17, all but the first term on the right may be ocitted.

V-B-6 6 Calculated Mean Temperature Rise : It is assumed that any change in the total mass of water in the compartment during a run is negligible. A corollary of this is that the mass rate out of the compartment is equal to the mass rate in. A statement of the first law as applied to the compartment is C t = k[h,-E]-A U[T-7;} (22) where 7~ is the mean temperature of the conpartment, and C is its heat capacity. Changes in have a relatively small effect on h-f, which is therefore treated as a constant. Uponintegrating(22), 4 At 21T = WAhst AU [T - 7, 6 (23) r : hat 71s initially equal to the pool temperature T, and It is assume g increases linsarly with time. Ab [7-A Then =. (24) Combining (23) and (24) and rearranging, I'v'ah A bT = (2b) C+pyg 3 Ah andV were taken as 1050 Btu /lb. and 0.0277 Btu /ft sec 'F respectively for all calculations. The second term in the l deonominator is a relatively small part for all compartment runs. I -,en -,,-.,_,-,a.-, ..,-,--.,n.,-.-_-_-_--..,-,,,- w----,

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- g g m ,,,-i - L_, 1' I .h 9 l-el 4 =.!'s..I-l C-4,' F L zu L'.o h, fa Y a _- mn fjd : Li.w, 5 C94 m te ,. 4 6= I . f - j _ J u c-o ET_ > > i t.t i M g r-i i 4 w,9s-cp=.i..m .9 .a 1 [ =+ :

at -

ti i-l i c

J '

h "# ? Md :=M ' ff I '*^ C-M - - "F t-

.!]l d' N3 h

. !. j.; f ,1 - J. -4'.-.. l_f e ,._ L ;,. l :. i. . ! w: _ . n %,n n =u c,Mihc p i. .>i; F...g, "- 4.- r-2 M. 14 ~ -7 ' i

..j

'1 j _: (

1. { OL '

i-E= t \\ 1., 4 I Q i., I 'l '

l' 1 i..O v.h E5 Q.

( , i _. _. ~ P. . J ,o 648 .! s ? i, p !!' '"? ti _ -. ~ ~ ~. l j- .i ! h.. Nte @ ~~T

t... I t

,3 "? ! lt ! I l ~ ' ~ " - - ut IJ l .i j J; j .i it --.% c -g ' a= =v F I4 n~ - t 2.# t-( b . f.

j. i t

l . i i i

F q..#
3 1

6 i: 4r +1 i-1 -l ' i 4: j N-4 3 9 J l i = f: -f-i _4 1. j :.- '~I~I - My ..t. { . ] E, --=.m e v t -l, - i--l - q. p .-t i i i c j , ; e ; ,. 3_- i i 4 i "1 } p.

i.,Lbid1

. '. i.i 'l -r=4 r. i l 1 j' I i. !4 3 t I i l i I~l 3 =>

d.). I j

l pI.4- .l l ] .l t t-1 Il ~ - h i [, i '.(, .n I -2:. .~ i i l W q. 1 n a = ( j. I - ; 6 'l u.-- i i. 1 i a1 i i _ _i = 4 ,c 1-1 3 11 1 I! ! -i i t d2 <. I p 1: )- i+ l . i ,, i i i i i 4 Q._:i j a. i , i - _- i .- t _ r,g i ; i __ ). -,-m,-

1HANb1hMI 1hST FACII.ITY .<.r ' _s t*,,'C,* t .p "'U'*11 U9 i J.3 -"tev9 tm g _y-* M F N-.J;p. -za ;p _s_ i2.i, u.J

O s.I' Lip

,,.ir": 1

m

.1 ' [9 a 's_ i .si .j, .'ca + E ..+ , t + ,,..f. .r. g ! -'_t ,gl. 4..., 'IL E I In[ '. ~ly.., ,k. y g .54.. ..I' j asi l ' i . l.t t i e J.' l 3 j L. -1} Y'. .a.. .]i.f-hg, Qf ..,i i.,c-q i _' '. _)y',,, .jg, 'qb_;qr a -.d (; /. U <r 3r. a 3,s. ..a .~. m........,,, a,-m. c i . i,,, < 4 .. nil . L

,,: ye' a...,

qt n F w 2.. . c .y i Ymaaa ,,.,i,,. .,gg. _ !!. i,. (s. e *. ',I f d g_ (y4 gwaqt g 3 - e 1 C i+ i .r c .i - m. ..i g 1 [,- .c .i c g. w. e s. u. A.. a ,z .i s i W a".c_i . av o x H i + e w en 6. n . A R.:..m..o o - ,a < > e eu + ... as = .i r-e, .i .,3 r_, ..__y i. .t 4-1- e i . u 2 e i s r u ia . ~ ri. i , i. a i + 3 c,.. L 6 .,4. d' ^ l p I f. ma L. p 4.. j,' f .i' s i g +; ! h ,, '. J.: j 9 :.

r-t *"

i ~4 i t-6: h .-g 3., p- . w. i.. 3 .4, {. . 4 e a p. i <.,i ,,i m. .f ,i. + r r.n._ i 4 c,s

.2,.

i...,. .n.. _,j i

i.

- o n. [ I 1!'1 N! L- ,l' .J a i - ~, ' 9- 'a f'~ .t! 4 . r. . ;l e j.. ,,gl

is

. i t. .o q e 5 i .d.. .; ai ., i. v, u

2....

.,g c g ,y

s. m.s.y,i w

~ .g c.-, a,; . i. .r f . r :.u,.;.,i i + .ci .A e 1. 3_ u a, g .l t '" . -ii i, - Ul i. p.;. 1 i, q 1.., nl-i. d, e

i....

_a_ _ m... .=- r i.i.!.F zi o j, r. t ~r I 'l e a. q o i .1 r i 3 4 i n., .p .h.._ _.i.} p', [ f { ,_F-, j. '1, j i ii I- .I

l. i 1

l h g, J - p t i; iL,

r,.13 Fr-i i

i i i i i i_.. < .,a :.: 4- .i ,y i i i iii 2 .1 'LJ41 {.; l f l 3 L._ . _.. 4 s n,

1.,,

r i 3 3..1 r 2_. n,e. 4 i. i i . j e r i -.. ; i- .i--. 1.. i. r e u c i 1 I I. k _e I s.. . 2,. [ .N .s g ./ I_ . l. I i .i _.q _ _1._ t..,r3 _' _.yk.

}': l... [

...i.., . _,.1 L .] _..ip -',_p. 4 4. '. L a, L _7,_.q._._ ..p,, ;, }... 9 p _...9-4__.. 3 .p._p.;_. ; i. _. y. 4_. . 1. t. 4_j _ p 9 4.g j.,,.. - 4 7,_.. 1.' 3 ..._. r 1.;. is

L'a4 1

... p 1_.i.,. Ir .u '. '.--.. ' - ~ ~ " ~ L, p_. - - _'... r r,..... .._ ___L . t, 1 Li i - i 21 i i u 1 .._L. _...L.. *...j ],3. i. j_ , t .2 i 4

; ;_ g.29...

i .,p. ,i 4. -4 y ..s__,- F T G1 %.-~ ) ('.y

V-D-1 APPENDIX V-D Transient Pressure Analysis The maximum credible accident is the complete severance of one of the lines entering the reactor vessel or an equivalent break in the reactor vessel itself. It may be shown that the worst case is a break near the bottom of the vessel. 'Ihe case considered in this analysis is a break in the bottom of the reactor vessel. A sudden rupture of the vessel bottom msults in expulsion of water s through the break, which is treated here as an orifice. It is ~ assumed that single phase water at the state in the reactor flows through the crifice before it flashes to steam. Heat transfer and storage in the syste= boundaries is neglected in the analysis, which tends to yield a conservative result. Actually heat could be absorbed by the dry well valls which would mduce the pressure and ter:perature 1 inside the dry well. All friction losses are neglected. 'Ihe analysis is based on one-dimensional flow. It is assumed that no mixing takes place between the pool water, the air, or the steamjvater mixture. This enables the air volume to be treated as a perfect gas undercoing reversible, isentropic changes before the pool vnter is completely expelled from the vent. If the air and steam / water were a homoCencous mixture throughout the dry well, the resulting pressure I basedon partial oressures vould be slightly greater than that predicted by the assu=ption of non-mixinc. Calculations show that for the rance of parameters we are considering, the effect of mixing on the pressure is slight. 1. "A New Approacr. to the design of Containment Shells for Atomic Power Plants", A. Kolflat and k*. A.Chittenden,19th Annual American Power Conference, March 27-29, 1957 i

V-D-2 Unif ru pressure is as umed to prevail throughout, th2 dry well to th2 vent inlet. It is further assumed that the steam / water mixture in the dry well is homogeneous and in thermodynamic equilibrium until the end of Phase B (i.e., until the air is purged from the dry well). The pressure at the vent outlet is assumed equal to the hydrostatic pressure which exists before the onset of the transient plus the pressure acting on the surface of the pool water, i.e., the contain-ment pressure. 'Ihe c ntainment pressure will increase during Phase B (see below) due to the transfer of dryvell air to the containment volume. Tae mass inflow to the system occurs in two phases: Phase 1: Occurrence of vessel rupture to expulsion of last of reactor liquid phase from vessel. (Note that break assumed in bottom of vessel Phase 2: From end of Phase 1 to end of transient. '1he mass rates from the reactor and the corresponding enthalpies are obtained as functions of time. Phase 1 neglects pressure increases l l in the dry well. Phase 2 is based on critical velocity through the orifice for most of the interval. When the velocity drops to subsonic, l the pressure in the dry well is taken to be atmospheric. l ( I Considering first Phase 1, the reactor mass rate and tathalpy are found as tim-dependent functions by a stepvise procedure. Reactor Vesh Stea= fv Water l l l L Ag, Area of break Vu, Water Velocity I t

The initial vessel pressure %0 provides values for V4 and k( 8 4

k (,Yv)

M

4JW) 4 The vessel agture is assumed to earrespeed to a sharpW orifice.

it is forther assmed that the flew through the orifice is single pbsse, i.e., that ne flashing ossure in the erifiset. The initial velocity of s unter essaping through the erifice ise

u. =

/ 2 3 v4 he d ere it is assumed that the dry us11 pressure P is eas11 in angni-tude, and that the process is quasi-eteady fisw for small incremsats of time. The earresponding asas rate is e w s 4 Aa K 1 9 I Succeerive time increments At are chosen to determine corresponding most rates and enthalples at the end of each interval. tyleying the previevely found W, the mass. of wate.- **meining in the reacter at l the end of At is : l t o + { U At. W=w tso f Notation appears in table at end of Appendix 0. 2. "The Flow of Saturated unter Through Throttling Orifices

i M. W. DeMamie and J. G. Miller 3 July,1941, ABE Traasaettems.

l

Emplayise previous values for both mass r;te and enthalpy, o see value ( et internal energy iss psa The specific internal energy of the mixture reesining in the vessel is found by E es -W i and the speelfte volane by i s Vv V' a -W These two thesmedynamie soeediantes fin the state of the resster fluid st a time tw= % + at, and the corresponding !a deter-ataed. hn provides now valus,s for 4 and A4..The procedure is repeated until V reaches the value Vs' at e leb time the liquid phase is gens fram the reactor, and the rensining steam is at 105 quality. Considering next Ftbase 2, again a stepsise proce&re is used to obtain the reactor esas rate and enthalpy as tias dependent functions, from i the time een the liquid level has reached aero. It is assimed that i atmospheric pressure exists in the dry well. i Sonic velocity will occur under the condition that y I P,, f,[0ti4 2. y_g Py ) j Beginning with pressure Pvt i l l l l

at the end cf Phase 1, carresponding values for V 5 and e.g are determined. r L T3

k (Pv) g s = 444 e

The asse rate for seats volesity to given by _t &. u, (n2 w N"F,',. O qv g (va s (1 ) A HY The seight of steam and the internal energy remaining in the vessel are, respectively, b Ws Em WE 3 Y$ AD is the difference between the immediate and preceding values i of P it to selected arbitrarily for each step. AW and AE are feend from oP. t Taor. 4t.

4W E *Q AL J

The energy rate is also given by E=kh l d le the specific stagnation enthalpy of the steam /seter shore flowing thro @ the break. sel.i.e for A, 4 ( k 4 AW e

,-+wr-

-v-w=-r,

e e we-v+-=we-----

-=--=c

A mes pressure lassement is agleyed, and the procedure is repeated, yielding values of h and M for earrespondtag values for

t..

mN sa 1 a.t i >l'td+",,..si. flew begins, and the asse rate is given by -{ f W M [b h [I I IP h 2 w= KA.< 1 i t- \\ W ~l duY o Pv. (% I ( hd ( w The same procedure is fellemed as uhen the flew use sents. The transient in the dry well takes place la three successin phases M Vessel rgture to complete expulsion of pool water from wnt. M Expulsion of air from vent. M Impulsion of stesa/wster from vent. The system which se are concerned with in this analysis is cogosed of the stoes/wster, the air, and pool water dich fall inside the beendary provided by th>J dry well enclosure, exhaust vent, and the reactor vessel. An idea 11:stion of this system is shown below: Vessel all (Rupture occurs bere) Air Pool Water i 'X Dry Well Vent Idaalize4 Svsiam The dry well is initially filled with air, and pool water exists at same lowl in the vent. i

thame_As \\ A agture ecours in the..ww30:1 and vessel fluid is espelled,to the dry sall. shame it. flashes to a hemogeneous aiutare of steam and unter. The day sell air is sempressed, and the pool ester is pushed bem the vent. There is as staing between the system campenents. The air volume is bounded by the fined system boundary and the interfaces at the pool unter and at the steanMter misture. Flow of the system cesponents 4 tossed the exit is one dimensional. Steam / water g g a. .3 I I 5-T~n - ~ ~ - - W Air 4, speel unter A

y-7..*

3i Ag P3 --T 1 e Xst V. -W r - L The assa rate of steam / water misture into the dry well is ha a-h l and the stagnation enthalpy is k, both of shich are time dependent functions. (See phases 1 and 2) The total internal energy transferred to the dry well in t seceeds, neglecting the wiecity in the dry sell is t (A. w. - ev. At a) Es J from the first law of thermodynsaics. The total mass of water treas-ferred to the dry well is ~ t N* b.O (2) O 1 l l 1 1 na we*~~e-.

V-D-8 Combining (1) and (2), the cpecific intarnal snergy cf the water in the dry well is EN c# = WN (3) he quality of the water in the dry well is found by CN~C/ (k) Off where Cf and efy are functions of dry well pressure. he volume of the steam / water mixture in the dry well in V8 = We r; and the volume rate is found by differentiation: (a WM Vp + G We Vy = hg may be written as YN and (6) % = vf

xs V7,7 (7)

Ye = Xx ty + vi,xe li ible. CombininC (6) and (7) with ($), the where is neC 6 volume rate become: Vy = Wr (xdy + rij g)+ N,(r; + x,q) k he quality rate is found by differentiating (4): Gn - C r eg4-(9) Xx = xx % DJ 4 l L

The specific intcrnal cnergy rato is obtained fram (1) cnd (3): c', e h- "" -- Y (10) Wu Wu The latent and saturation property rates may be written as cW h V45 p P (11) (g (12) 4 (13) b t* A relationship is obtained between and P during Phase A by considering the air volume, uhose asse is constant. w C. o w %T. (14) W g r. W Ao The voltane of the air during Phase A is t 0A dt (15) V A* Vao + s' uhere Q, = h s - h (16) Assuming an adiabatic process, the air pressure is yl (17) P ' P. ..r.. ..t. r

Y* V ^

y$ us) p-Va " l

cambiatas (4), (s), (9), -(to), (11), (12), (13), (16) and (le), y (, l.fi A 4.w -I.ht. + +4 Y Wa P.v.. V' v.r+i (,,, gg x .t,} w. v w va ' i - v, m Va and P are reisted W further eensideretten et the ate and pool water. Applying Ruler's equation to the air, l g f 8 P + k b (4*) + % l + b b %, u, c (20) ~ Integrating each term between two points, and recalling that f = 4(P) bP + k(42-MI) + $(,h-si) +[ h A ro (21) P xi All the air oss initially st the same state. Assuming that it under-goes an Asentropic, reversible process, the serresponding thesmodynamic coerdinates are time functions as well as point functions. The follow-l ing is substituted in the fire ist rs! P. ~ 4 J. P i =. o r s $(Bs-D d and are neglected to give Beth ~ l At E3 d p p +% 9 D%eo 1 r. t-s u .\\ z a = Ki

m. rrang.d,

_y d 3 M r s rh fo P. + Ps= P (22) x. i I

~ 0=G Espanding by the hinsairl theorem, P s P - P.f. P. (Y + , bx +-- (za) ( i Just the first two terms will be used for conservatism and sinplicity. 1 DX is next. evaluated. 'ho assa rate at any section of g the vent is k = f M As and YA f A a. Differentiating, SM e -N R fAu et f et (24) Prem continuity relationships, ' = Na -(VIA + N A dt) DSA 4K bt tA 6x Also b,y,A, As ay, 6._{ i bt bt. 4 aber. As J W, is a volume element fixed in space, independent of time. Combining, l bf A TI,.1 (25) At b x, t Ilent, cambining (24) and (25), i hu *. Tis k A Na h 8da) t t ~b'"E Ti (26) i i l l t- ,~--wre-7m, w e.r m .wm--., me e enmm

V-D-12 Assume now that g is independent of ,X and substitute .l$L * [ which is conservative. " dX f (29) The mass rate of the air at point 2 is 4$2 (30) /44, = /.r. #2 Differentiating with respect to time, d$s dA di ~ di #' #'

diduab #* * ^dtd'A "' A (31)

OY dwe = Vz gf, ltV + y-(32) dp 2 l l n,,, ., --w. ,----...-.---,,-,-,,n .,.,,,------,-----,,,.-.,...,w-,

Combining with (29), g g Ys + s 4% 46 A t Ks A pL ( + y, d b ls). D dA a t g, As (33) 4s s g, A = A V,)k9, <=> >.. s*. sis.tia. A A D d K

m., ks + Y.

r' 3' .h h. t t. L 1r Ps, A ' At (34) t, j 1 se here assimme As

1. = linear funetten af Xs As = A.-Ka'8a (35) from which At j

K s4 (36) A i Cambining (34) and (36) with (23), assuming that 9 = P-9s. = ($, [g*g* 0,.+(g,'(* (*i X, + h (37) i An expreselon relating P.3,, and P3 anay be found by applying Euler's equation to the pool water M3 w N w) + 5-A +y,s (4-w?)+y ['d 0* =a e (38) Ws The mass rate of peel water at point 2 is [g.Ma. * [t A s u-W t gs from which h en* (39) As

Differentiettag with seepest to time, reselling that As is a function of h, saly, and membintag with (35), 4.S = V h. (m) h As. A.- % k, men eestismity. ut As

Ms. As A

u e, A% s h w?-w? - { {I, - l$Md but .y's t hsus At Ms g i Thererere, . s. w3 - u) = ((Ys ~I (**) ,l I cashining (41) and (m) with (as), .s Is-h2-WP(,h-ts) h, ',; g' b (42) 511mipsting 73 by the cambination of (37) and (42), the resulting i. expression una solved for Vs and integrated to obtain an expres-sien, f,or ha.. L-ks oss substituted for Es-1,. t, 07%)\\9, + (9,$-i zb - b,(t-hb-d-4% - A 9'f4 -i M. t) - A ( %) + rbe#'- g i gq'3 dt. (43) --),f [, -I M k)-M(k) Phase A is ended uten )( s L.

mai u. e.a s.r i. - er. a. .s.w or.s.rs. i. m. 3..su i.t. me pool. Go I '.i.h '.. N -I ~ 9 A -+ sa.,, ' I ^1' A 3 3 \\/ P,' eg ,... r.4.t a. a,.t of a. v.ni, is r..ier a.. r..i to the critical pr.ssure with r.spect to P . If P is great .n. ugh, T' is critical and 3 i f L u-t p3 4 p3 3. I (44) y 9 W+\\ Considering the subsonic case, the mass rate of air in the dry w.11 is As Ms [3 (4) [w 5-f Re-.rranging and substituting l s. I f \\9

s. 4 (46) 3 Ai, LA g is giv.n by

~y gF V.::1 a. I (C) L.13= R ,, g l uh.re A is the sonic velocity under stagnation conditions. k kY h (M) k* h bT I 6 l l 1

s s Assuming that the ctr endesgees a *resesible, Seestrepic pretees, (EY m, % \\% v s and estving ter PV. g_ A. Pv = Pa

v. P (49) su ettsutine (4e) inte (m),

d = b a r b. ' e 5 1 g .it,(4,), 1:! 1 lk (51) T g P. v, y M9: i w -s .i l subettsutt'ap inte (46), t-hi) (52) 't h % P t In order to consider the sonic cose, the fellowing substitution sust he made for la(52): .E_ %~\\ ,f' )9 T, Q +t 9 4 dich gives g w-i r ir a a .1 = 0 Y g ?.g v. I p P (ea) Y. i 4 4 Eggstions (52) er* (53) are selved for Vx. Iquetter.s(8),(9),(40), l (11), (12), and (13) are tambined and errenged to giw en espreselon for f' dish ~1s then 1M,ograted to give P. The ef fect of a stem /sator mixture entering the vent will be neglect <d i i I 1

,------.-----,,------m-_,---vv.--=

~ m-- , we v -

l l V-D-17 s - i until all air is expelled, or until t ^ 'N f o f = (54) at which time Fnese B is ended. Coincident with the expulsion of air from the dry well is the addition of air to the containment volume and the attendant rise in containment pressure. This produces a correspor. ding rise in s the pressum at the vent exit. f.s = fc tW4 (55) p The containment pressure is increased slightly during Phase A l pc, = po ( y ) (56) VC refers to the volu:ne of air above the pool, which is reduced during Phase A due to the expulsion of water from the vent. Let T be the fraction of dry well air at any instant which has mixed with the containment air. Assume complete adiabatic mixin6- '1 hen, per the first law, Ec = Eci + r Wso Asc 'f'[(f,") + rWas bse (57) = Eco + But Ec = [rWoo t Weo] c c (58) s //4,= P. W + C * (59) l l

s t ( l v-n-18 : combining (57), (58), ard (59), c ] We,{ee -ce, - j'.f' (((,',') l}) = TWoo[M-lec-e.) (60) It is assussed that the initial containment pressure and temperature are the same as for the dry well. Sen fee = C,, A, = f, Fe Letting A e = cya [ and substituting in (60), \\ and Tc, = Vc,[c,(r -n)- gg.Q..$ IQ= rVso[n-c,(r,-,7)) e i This may be rearranged to give ~l Vce t V'* Veo + No which reduces to i l Vce j __ Veo (61) I j, = y VC*ff VRO f Vet / Vee +-r % o he containment pressure is given by ?' ~- (fW* +%)}?7c _ f' x y%, (r%o+ %o) "Tc' Vci ye, (62) a, combinin6 (61) and (62) a = r. ?:[r ? + d] p.[rt + (gf] () = At the end of Phase B the containment pressure is given simply by fo f$ + V'*) (64) fc = The pressure at vent exit is given by equation (55). i l l

V-D-19 i Phase C: j i The last of the air passes out of the vent, and steam starts to be ejected. j i This part of the transient is tnated as quasi-steady state. Two special assumptions am made: (1) The steam / water is no longer i homogeneous, but undergoes complete separation in the dry well, a o (2) only the vapor phase flows out of the dry well. he pmssure l is uniform throughout the dry well at any instant, and flow through I the vent is reversible and isentropic, both assumptions made pre-viously. Ist the rate of heat transfer from the dry well be Q. Ren, i treating the dry well as a thermodynamic system and applying the first law, a o fy = Wy h - W, h, - Q (65) but (66) C Cy+ y4 f y (Note that e is the saturation value corresponding to f the dry well pressure p. But the average internal energy of the liquid phase in the dry well may be different. In this annivsis the average may be higher er lower than the saturation value. This assumes ne61181ble flashing in the event of a drop in dry well pmssun.) 4 he total steam / water volume [g is equal to the dry well volume, hence constant. Therefon e V H J g or .W = - ir y/ (67) J J l --ege. ~. -,-,,_w.. -_,e,. yy.,c,--- ,.,-----y-,.,,--mm..,n .,, ~.,,,_. ~,_ y y,- --9 ,.y

V-D-20 From conservation of asss principles g .W-W W, 4 W = ll g W, (68) = 4 u 3 combining (65),(66),(67),and(68) W,b - i l,h,- Q = e' j< e' [V's -W,] (69) r v, hy/) - k ~ N (70) l Let t e'- -@V} e l Z_f ) (71) l /-$ N, h,-R, f(p) = C (P) (' ) Then b (73) X i [f t hg and b are given functions of time. k can be estimated. A and [ y are known, hence h is a function y y of f, pemitting the representation, as given by equation (72). Equation (73) must now be solvec. for p. A convenient way of doing this is to plot p-fy, versus ha for a given value [7 and M , and various values of [. of y In preparing the plot, must be detemined. From energy considera-y

tions, N, =

[2y (4,- h,)' (74) State 3 is at the vent exit. It is determined from the pressure and the entropy 5,, given by 5

S (75) 3 yS-S s

o y 3 __ 3 9y (76) = W qs # A A O 4 (g) 3 v'y = Y, 9p 4 "is

V-D-21 Results The equations for Phases A and B have been arranged for numerical solution by an IBM 650 computer, and for Phase C by desk calculator. Solutions have been obtained for the same parameter combinations as employed in the Traasient Test Facility. Comparison between these g and the test Itsults appear in the text of this report. u k 4

V-D-22 NOTATION l Dot notation is used throughout to npresent to tim derivatives of functions. Symbols l; l M Ana (sq. ft.) 4 Sonicvelocity,stagnationconditions(ft/sec) l, I E Total internal energy (ft. Ib.) ~ C Specific international energy (ft. lb/lb) 4 [ Function of pressure 6 Mass flow rate per unit ama (lb/sec/sq. ft.) f Gravitational constant (ft/sq. see) M Enthalpy (ft. lb/lb) Ne vent constant (ft) /_ SubmerEed length of vent (ft) 8 Pressure (lb/sq. ft.), dry well pressure without subscript Q Eeat (BW) 5 Entropy (Bw/deg.R) 7~ Absolute temperatures (deg.R) 8 Time (sec) 4 Velocity (ft/sec) V Volume (cu. ft) i l V Specifievolume(cuft/lb) 2 W Weight (1b) O Wei ht density (1b/cu. ft.) 6 )[g Quality of steam / water mixture in dry well (vt. fraction) l Xz Pool water displacement from original level (ft) E Pool water elevation above arbitrary datum (ft) T Ratio of specific heats l l

V-D-23 i Symbols (continued) [ Massdensity(Slugs /cu.ft.) Subscripts A Air 8 Break in vessel i C containment vessel o f Liquid phase a [g Vaporization f Vapor Phase // Dry Well (absence of subscript may also nfer to drywell) O original state before onset of transient [ Pool V Reactor vessel 1 Inlet to, or upstream of, vent, end of Phace A 2 Interface between pool water and air, end of Phase B 5 Exit of vent O 4 e 1

bw MVl 6 l Fts-veoum O I f m-psup v s h 3 3 I ,pe ) i = p p ~ ~ ~ ~ [ ~ 1 t p... L-FGM v =, i_ N .J a - ~ b.. _ T.. l FE ' en e ; ,I..it

u. _-.

t

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ML20207T985

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ML20207T985

Text

Dear Mr. Thomas:

Enclosures:

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