ML19351A119
| ML19351A119 | |
| Person / Time | |
|---|---|
| Site: | Palisades  |
| Issue date: | 05/01/1981 |
| From: | Vreeland D LAWRENCE LIVERMORE NATIONAL LABORATORY |
| To: | Chang Li Office of Nuclear Reactor Regulation |
| Shared Package | |
| ML18046A745 | List: |
| References | |
| CON-FIN-A-0241, CON-FIN-A-241, TASK-06-02.D, TASK-06-03, TASK-6-2.D, TASK-6-3, TASK-RR NUDOCS 8106250286 | |
| Download: ML19351A119 (67) | |
Text
{{#Wiki_filter:. [j i Lawrence Livermcre National Laboratory
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' May 1:, 1981 I -
u ,,- m n Mr. Chang L4- - Containment Systems Branch (Division of Operating Reactors . Office of Nucigar-. Reactor Regulation U.S. Nuclear Regulatory Commission Washington, D.C. 20555
Subject:
FIN A0241 Containment Analysis Support for the Systematic Evaluation Program. Main Steam Line Break Analysis, !!SLS, for Blowdown of One Steam Generator .
References:
- 1. Palisades Plant--Autcmatic Initiation of Auxiliary Feedwater System at Palisades Plant, Docket 50-255 License DPR-20, January 21, 1950 letter from R. W.
Huston of Consumers Power Co. to Dennis L. Zieman of NRR, NRC.'
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'2. Pal'isades Plant--Proposed Technical Specifications 1 Change Related to Containment Spray Initiation Time, Docket 50-255 License OPR-20, November 24, 1980 letter from D. P. Hoffman of Consumers Power Co. to D.
Crutchfield of NRC.
Dear Mr. Li:
Attached is the MSLS analysis for the blowdown of cne steam generator. l This would be the wr st case analyzed provided a fix was imposed to prevent both steam generators from blowing down. Iri this case -he single failure would be loss-of-offsite power with a diesel generator failure. The available containment heat removal system would then be reduced to l two spray pumps and one air f an cooler. The mass and energy release' data l l used in this analysis were taken from ref. 1. The assumptions that went into arriving at these mass and energy release rates were found to be conservative and in agreement with the SRP proviced a failure cf a MSIV is not considered. The assumptions used in the containment response calculation are based on the proposed techni' cal specifications discussed in ref. 2 The results of our analysis show that the calculated peak pressure is The 58.5 psia reached at 67 seconds. This 1.2 psi below design. Therefore, calculated peak temperature is 4130F reached at 37 seconds. based on this analysis, a fix which would prevent the blowdcwn of both steam generators would limit the calculated peak pressure to 1.2 psia below design. . Yours truly, ew l- . Davi: resianc
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Principle Investica:or Attachment .
-G. Cummings 22.Q er. 2 Rev m n 8106250-h N
Enclosure 1 SEP Containment Analysis and Evaluation for the. Palisades Nuclear Power Plant Contents Page . l 1.0 Introduction and Background 2 2.0 Containment Functional Design 2 l 2.1 Review of Palisades Containment Design Analysis 3
- 2.2 Primary System Pipe Break 3 2.3 Secondary System Pipe Break '4 - - 2.4 Reanalysis of Palisades Containment Design 4 l
3.0 Primary System Pipe Break 5 3.1 Initial and Boundary Conditions 5 6 3.2 Blowdown Phase 7 l 3.3 Reflood Phase - ! 3.4 Post-Reflood and Containment Response Calculation 9 3.5 Containment Resp ~onse Resul.ts 14 l 4.0 Secondary System Pipe Break 16 4.l' Assumptions 17 4.2 Containment Response Results 18 , 1 . 4 I = i I O e
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1.0 Introduction and. Background , On January 1,1980 the Office of Nuclear Reactor Regulation (GRR) initiated a two-year program.with , Lawrence Livermore National Laboratory {LLNL) titled Containment Analysis . Support for the Systematic Evaluation Program (SEP), *This program is directed toward resolution of SEP Safety Topic VI-2.0, Mass and Energy Release for Possible Pipe Break Inside Containment, and Safety Topic VI-3, Containment Pressure and Heat Removal Capability. The containment structure encloses tne reactor system and is the final barrier against the release of radioactive fission products in the event of an accidant. The containment structure must, therefore, be capable of withstanding, without loss of function, the pressure an'd temperature . conditions resulting frem postulated LOCA and steam line break accidents. Furthermore, quipment having a post-accident safety function must be envircnmentally qualified for the resulting adverse pressure and temperature
. . . M conditions. To accomplish the objectives of jiiWprogrim, first, .the' existing docket informaticn was reviewed and evaluated and then additicnal analyses as were performed r required. The purpose of this 2 port is to document original analyses performed by the LLML on the containment functional design capability
! of the Palisades Nuclear Power Plant and evaluate existik, analyse [for
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conformance with current NRC criteria.,.~a--~ . . .
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'2.0 Centainment Functional Des'icn ,
( Palisades is a Combustion Engineering PWR licensed to operate at 2200 MWt. The primary coolant system is a two loop system censisting of two steam generators with two cold leg icops per steam generator. The con ainment
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i systems include the containmerjt structure and associated systems. These systems include containment heat remo' val systems, centainment isolation systems and a ccmbustible gas control system. l
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r; 2 F- .: .. 6 i;k % . r0 J n .- The containment is a steel-lined, pre-stress , o . . -t einsion concrete structure with a net free volume of 1,540,000 cubic feet. The containment structure houses the nuclear. steam. supply system; including the reactor, steam generators, reactor coolant pumps and pressurizer, as well as certain components of- t$e' engineered safety fe'atures systems. The containment is designed for an internal pressure of 55 psig and a temperature of 2830F. 2.1 Review of Palisades' Containment Desion Analysis There are two separate calculations which make up the containment design an alysis. First is the mass and energy release analysis for postulated ( LOCA's. This consists of a blowdown, reficod and post-reflood phases. The results are mass and energy release rates into the containment. For PWR's there are two possible break types which must be analyzed, a primaiy system pipe break and a secondary system pipe break. A break on the pri' mary side
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generally results in the most . severe pre'ssure,"Yi!fponse in the contaibent i while a break on the ' secondary side results in the most severe temperature l i conditions in the containment. The second calculation which is per. formed in the centainment design analysis is the containment respcase calculation. This i i results in the containment temperature and pressure response to the mass an'd
, energy . release from the postulated breaks. .
l
. The acceptance criteria used to evaluate Palisades' Containment Design
\ - l Analysis was based on the Standard Review Plan (SRP). In order for the l containment design analysis to be found acceptable both the mass and energy ( , release and containment respcnse calculation must meet the acceptance criteria specified in the SRP. . i 2.2 Primary system Pice Break The SRP specifies several acceptance criteria applied to the mass and ! energy release analysis for primary system pipe breaks. li.cng these are break
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calculated for containment design was done assuming a double-ended cold leg
. discharge break with no accounting.for the refloo'd phase or energy in the s,eenndary system. Since 1.his does not meet the acceptance criteria specif,ied i t. t.he SRP or previously accepted methods by the t'RC staff, this analysis is unsuitable for containment design calculation. Since the mass and energy release rate analysis is found unacceptable, so is the containment ~ response calculation based on the mass and energy release rates.
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2.3 Secondary System Pipe Break , The most recent secondary system pipe break analysis that was reviewed was submitted by Consumers Power Co. to the U.S. NRC on January 21, 1980.1 In this analysis'a main steam line break (PSLS) analysis was performed. In this analysis the blowdown of one steam generator with feedwater isoliticn and
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loss-of-cffsite power was considered. . Howeverbe analysis did not address, the possibilii:y of a single failure of one of the main steam isolation valves which could lead to the blowcr..n of both steam generators. Therefore, the analysis was considered incomplete and' unacceptable. A more thorough discussion of the MSLS analysis is given in Section 4.0, Secondary System Pipe
, Breaks. .
2.'4 Reanalysis of Palisades' Containment Desian As mentioned earlier in Section 2.1, Review of Palisades' Containment
. Analysis, there are two separate calculations wh ch i ma ke up the containment design analysis, the mass and energy release rate and the containment 1 Palisades Plant - Autmoatic Initiation of Auxiliary Ferdwater Ssytem at Palisades Pl'nt, a Docket 50-255 - License DPR-20, January 21, 1950 1etter frca Roger W. Huston of Consumers Pci:er Co. to Dennis L. Zisman of NRR, L -
NRC. i l
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li!! :1y aj'ih. r18 p w: 3.- ay response. The mass and encrgy release rate calculation can be the result of
* - either a primary or secondary pipe break. The primah pipe break generally results in the limiting condition for calculating the peak pressure inside the
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containment. The secondary pipe break analysis generally is the cost limiting case for tempera.ture conditions inside the containment. Both of these ' l analyses were performed and are discussed below. l 3.0 Primary System pioe Break l For a primary system pipe break there are three phases in calculating mass l and energy release rates. These are the blowdown,'reflood, and post-ref.lood phases. In each of these phases the calculation was done in accordance with j socic- t.z.s.5 *f L . St~ 4 :4 . k ie, a la g , 4 the q 7:re ; ::% under the const,r-adt,of the computer codes used.a In l p general, the analysis was done in a manner that conservatively establishes the sc.
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containment design pressure; i.e.,, maximizes the post-accident containment 4
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p 3.1 Inftial and Boundary Conditions s , l the initial and beundary conditions for this analysis were defined to h' C satisfy the requirements of the Standard Review Plan. The single f ailure A assumptica for these analyses was a loss of one diesel Senerator. The initial power was specified to be 102% of safeguar'ds design rating or 2590.75 MWt. A steady-state mass and energy' distribution was provided in the primary and The secondary coolant systems consistent with the conservative core pcwer. ) break flows were calculated using a discharge coefficient of 1.0, with the
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i l l Henry-Fauske correlation for subcooled and the' Moody correlation for saturated fluid. The safety injection flows were minimum, corresp:nding to -the diesel The mass and energy release analysis was performed with cenerator f atiure. kELAP4M005. Steam quenching by the. safety injection water cccurred due 'tc l .. . l
- li & M li~Y p2!E3,iEit? I:
b,#d LA'U d the homogeneous equilibrium (HEM) assumptions of the RELAPA.M006 coda. All of the safety injection water temperatures were defined to be 900F. Scram was assume'd to occur with a low pressur'izer pressure of 1750 psia. , A 1.0-second delay time was used in the medel for conservatism; however, the moderator reactNify feedback caused core shutdown befcre the control rods were effective. The main coolant pump power was tripped cff at the time of the break. Steam generator isolation was initiated one second after the break and the valves were assumed to complately close in five seccnds. A 15-psia
.constarit ' containment backpressure was assumed to maximize mass and energy release throughout the clowdown. The end of blowdown was defined as, the time the primary system pressure reached the containment design pressure of 55 psiij.
a d m; c.wl V.,fermation,uvined far co The RELAP4 input deck was chtained frem fiRC3 . Additional i'n g.4s required for the analysis was obtained frca the Palisades FSAR, and telephone - t W 3 : T w T' conversatiens with C. Tinkler of NRC and D. Vandewalle cf ConsumWs Power
, M $F 2
Company. A thorough discussion of the model'dFfe fcund in the Meth3dology h
\L Report for the Palis'ades Nuclear Power Plant. 2 o%
! P 3.2 51cwdown Phase
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The bicwdown analysis results are summarized in Table 3.1 and Figures 3.1 %i
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,through 3.4. Table 3.1 itemizes the energy sources for the duration of the g[
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blewdown which ended at 20.4 seconds af tar the break. The total energy f{s released during blowdown was approximately 253.4 millien Stu. Figures 3.1 ,,' A.C D' thrcush 3.4 provide break flow and enthalpy cut the break. AK ra The accumulater flows start af ter 16 seconds and do not reach maximum flow rs 4
.D rates by the end-cf-bicwdown. The pumps coast dcwn at different rates. The ' 4 pu p nearest the break reaches zero rpm before two seconds because of reverse hf -
( flow thrcugh the pump. The pumps were not allowed to reverse, providing a { ccnservatively high resistance which allc7:s more flow through the steam 6-y --m- .,.7 . , , . - a 9 y .-w yw-e g - -,9w y *w - --my i
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' generator side of'the break. The othcr pump in the broken icop coasts down to zero rpm .at about 11 seconds. The pumps in the unbroke,n loop continue to have o
a positive rotation throughout the, blowdown, although it decreases to 500 rpm jnabout10 seconds. Although the . scram occurred at about eight seconds, . I moderator reactriity feedback had already reduced the power to less than 7-1/2% of the initial power. The mass and energy release rat s and energy sources were qualitatively compared to the CESSAR results for a double-ended suction leg slot break with the same area. The similarity of the results suggests the RELAP4 calculated blowdown results are reasonable. . 3.3 Reflood Phase u. The reflood analysis for the double-ended pump-s[ction break was assumed, to immediately follow the LOCA blowdcwn analysis , The analysis,Was performed using RELA?? M007. Within the limitations of,lbNAP4 M007, the analysis was performed in accordance with the requirements of Secticn 6.2. f the Standard Review Plan (SRP).- Initial conditions for the start of the reflood analysis were based on the end-of-bicwdown (EOS) results. EOS was defined to occur when the primary l . system pressure fell belcw the Palisades containment des'ign pressure of 55 psig
- which eccurred at 20.4 seconds af ter the start of blowdown. At that time, the core pcwer level had dropped to 159.41 MWt or approximately 5% of the initial pcwer. The accumulator ficws had been initiated on low cold leg pressure trips of 252.5 psia which occurred at about 16 seconds into the blowdown and l had reached a total of 5900 lbm/sec at the start of reflood. The reactor coclant pumps had coasted down and the rotors were loc,ked.
For the reflood analysis, the primary system was initialized at the containment design pressure, 69.7 psia. -The primary system junction flows
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UHMr H were zero except for-the accumulator and lower pNnum inlet, and outlet , junctions. Heat conductor temperature and primary system state conditions
' were established based on the EOS . conditions. Core power centinued to ,
decrease
;
according to the ANS decay heat curve. * . A natural. cEcuTation heat transfe'r model was used in the steam generator secondary to maximize the energy transfer rates to the break. The primary coolant pump. rotors were assumed locked to conservatively provide resistance to flow. A closed valve was modeled in the intact cold leg of the brcken loop to conservatively increase the flow through the steam generator.
'For numerical stability of the RELAP4 cc puter code, the Emergency do're Cooling System (ECCS) flow was modeled as being infected directly into the ,
downcomer at a temperature of 2000F. Plan.t specific information was predominantly derived frca a RELAP4 Reflood input listing for the Palisades power plant which was obtained from
, w the
, Nuclear Regulater Ccmmission.(NRC), and fr~omb Palisades Final. Safety analysis Report (FSAR).
Several sensitivity calculations were performed to evaluate varicus input model and code options. The results of the sensitivity studies are documented in the methodology report. The Palisades reficod transient results are
~s able 3.2 is a summary of
, presented in Table 3.2 and Figures 3.5 through 3.
the anargy balance at the beginning and end of reflood. Figures 3.5 through 3.5 provide break ficw and enthalpy out the break. , The accumulator ficw is initiated at 5900 lbm/sec and quickly rises to 6400 lbm/sec. The flow remains constant until 40 seconds, and than is ramped dcv.n to O lbm/sec at 50 seconds when the accumulater is empty. The HPI flow comes on at 0.6 seconds and remains at about 650 gal / min for the i'.uration of
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the transien't. The LPI flow ccmes en at 7.6 seconds and varies in magnitude between 400 and 600 lbm/sec for the duratton cf the transient, depending on the primary system pressure. .
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- The primary system pressure starts at 69.7. psia,.. increases to 160 psia at 20 seconds, and then slowly decreases to 100 psia. Th,e pressure increase can be attri.buted to steam binding in the primar.y sys' tem. As the ECCS water i
gnters the core, it boils away faster than the generated steam can eseape , through the bireak. After 20 seconds, the core is quenched and the steam generation rate reaches a new pseudo-steady-state with the break flow. Normally, the end of reflood is defined as the time when the core recovers to within two feet from the top of the core. In the case of Palisades, the 1 . l ,
. maximum mixture level is less than seven feet at 50+ seconds into the transient which'is still four feet below the tcp of the ll-foot core.
However, the core-stored energy was essentially removed at 30 seconds into the . tr ansient. The reflood calculation was extended to 100 seconds to determine when and if the steam generator side break flow would 5egin a rapid decay ' expected ,
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af ter the accumulators emptied at 50 secondi" %ce the-rapid flow decay did [ ' not occur, the reflood calculation was coatinued beyond the time when the l containment calculation predicts the peak pressure and temperature at 84 seccnds after break or 64 seconds af ter start of reflood. Because the safety injection water was assumed to be at 300C F, the extended duraticn of the j .reflood analysis is considered to provide t. conservatively high energy transfer rate to the secondary. 3.4 Post-Reflood and Containment Response Calculation
The containment model used was based on a CONTEMPT deck received from the ' ( - I NRC. The mass and energy flows to the containment were replaced and the i ' f remaining data carefully checked against the FSAR and other sources. The i analysis was performed using CONTEMPT-LT/028. l .- o e l
h MLN:f$. 0% cf' All the structures are
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The heat structures used are listed in Table 3.3. represented in rectangular geomatry. The thermal conductivity and the l volumetric heat capacity were checked for the four materials used: steel, concrete, insulation, and air (gap). The heat capacity was found to be about. two orders of;mirgnitude low for insulation and was changed. Tagami/Uchida boundary conditions were used for all heat structure surf aces except the base l u slab, which was assumed to be covered with. water. The Tagami peak time used was 20 seconds, 0.5 second before the end of blowdown. l l The basic assumption was that off-site power was lost and that ene diese? generator f ai%c' to start. The cooler and spray pump start times are bas *ed on the gener.ator ading sequence. 1 I It was assumed that ene f an ccoler was operating and that it started at 23 seconds af ter the break. ' The heat removal rate was variable, ranging from 97.5 M3tu/hr at a contain :ent temperature at 3500 F to 3.0 M3tu/hr at - l ,. 104cF. The one operating diesel generator Wash:tso' assumed capable. of powering two spray pumps. Both pumps together were capable cf 1.34 M1bm/hr (2700 gpm) with spray efficiency of 90%. The containment spray started at 84 seconds and used water from the Refueling Water Storage Tank until 30 minutes when the tank was empty, at which time the water source switched to the ) t,.vtc. .-<nt ce -vThe heat removal rate for the shell and tube heat exchanger in I dry.e:P pech the containment spray system is computed in CONTEMPT. The entered parameters were: the product of the heat exchange surface area and the overall heat i transfer coefficient was 2.28 M3tu/hr/F; the coolant inlet temperature was ll4 0F; and the coolant flow rate was 2.0 Mlbm/hr. y-l General initial conditions are given in Table 3. Initial conditions for the primary sys, tem refer to the end of bicwdown. No water was infroduced to g , .c a the dr;.:e+1 as an initial step input. The evaporation-condensation mcdel in the Aimef' r.!Pfe dl was bypassed until the end of blowdown. The fracticn of wall or i l 1 * - 10-f--, ,#y .-
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cooling coil condensate t. ransferred from the superheated t x.&1 mosphere %t to tK.-r$ie the pool .was set at 0.92. The heat and mass transfer multipliers were set at 1.0, and the temperature flash opt.icn was used. - Two methods of treating the post-reflood period were used for this .
;
analysis and .thhei different assumptions made about the mass and energy release during reflood, resulting in six cases. The blowdown mass and energy release was the same fo: alk cases. Peak flow was about 77,000 lbm/sec at 525 Stu/lbm, and the blowdown ended at 20.4 seconds. The reflood data # xLL c ms k lasted 100 seconds
;'- 120.4 seconds af ter the break. The cere was not covered, or even two-thirds covered at this time, but it was substantially .
l cooled. Therefore, the end of the RELAP4 reflood run was defined to be~ the
- l m ,&mgL end of reflood y the accumulator flow had been ramped down to zero between 60 and 70 seconds af ter the break.
1 During the post-raficed period, decay heat, r heat frca the secondary system, and heat frcm tr.e heat structures in',thFprimary syqtem are released l to the containment. The decay heat is released over the duratien of the run l . . l l based upon the ANS standard decay heat curve plus 20% and an ultimate reactor
- The power of 2636 K4t plus 2% for instrument error (excluding pump heat).
l - ? heat from the secondary system (61 M3tu) and the primary heat structures l
,(53 M5tu) was all released by one hour after the break.' A linear ramp to zara ~
was used. ! The amount of heat released to the containment by the secondary was determined by obtaining the stored energy in the water in steam generators and l in the SG tubes at the end of the RELAP4 reficed calculation. Assuming that l '
- this was based on 32 F and that the eccire steam generator would be at
~
2120 F. af ter cne hour, the amount of heat available to be released was This is conservative because the containment pressure
- computed to be 61 M5tu.
will not decrease to atmospheric pressure in one hour, and so the secondary e
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[w u .urnN h system will be hotten than 2120 F. 'For the primary heat structures, the. --
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energy stored in all of the heat structures used in the.reflood model, except It the core (fuel rods) and the steam generator tubes, was used in the model. 0 was conser'vatively assumed that all this metal would be at 212 F af ter ene I hour, with the differenc.e (53 M3tu) being released to the containment. Ouring the post-reficed period, two different methods were used which differ only i.n the manner in which the energy from the secondary system and primary heat structures is released af ter reflo-- In Method A,k' jev
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-d the energy is released di.ectly to c-cr 7
m;,,,,',,g wirked Cn.025iq +Id.'.: primary con % 7 s.ysTer.,
- the P Ar.::!'. The amount of mass accompanying this energy release is requtr'ed, and it :: obtained by assuming that the heat is used in converting water at saturation to steam. A typical value for the heat of vaporization at the pressures experienced in the containment for the first hour is 925 Btu /lbm, .
l -
- and this has been used to calculate the mass release rate. -~w This method is Lsrj=rly conservative, since after scme time thawater in the primar'y system will cool to below the boiling point and most of the decay heat will go into heating the water to saturation and leav'ng very little to gen'erate, steam .
gd.M The systems (HPIS and LPIS) that inject water into t;. primary are not modeled in Metho A since the mass and energy flow frcm the primary.is already calculated as described above. In Method B, k p+ry ::. g.-t...;;t -': ::t2 ;; i a ::.r"...--)..lthedecay C heat and heat from the secondary system and from the primary heat structures
+t.r y, 4. m dar e** W r sysrc.m is passed to the pr'- ry compartment 3,,The model in CONTEMPT then determines how much steam is produced, how much heat goes into increasing water 1
' temperature, and so on. This is much mere realistic than Method A since it allcws the steam production to decrease with time. , It is still conservative In since the heat input has been calculated to be 'conse'rvatively high. The L?IS Methcd 5, injection into the primary i.s explicitly modeled. F - p'+<-+g.y- -y. w%7=- y ---iw nv -g- p,g. e- , . ,g.., -g,.we+%w++9.wi.-%,,q.q-p me,yev---y---w.swyew.-- v--e.-ep--gveg--w-,wrw-v1me-v-u-- eem> wv--+--
O NM ('.h.u, 0 U.wh . 9 (5000 gpm) and the HFIS (450 gpm) both take water from the refueling water storage tank until it empties at 30 minutes. After that, only the HFIS ' continues, taking water fromy% I' the c. WG. .. 7::hecEW"here T is no heat excht.nger cedr*~-.s% .;-l-either of these systems. The dg.;;" ;;;l is gradually cooled Ar..s.:F9 since the water that is recirculated through the containment spray system does' pass through a heat exchanger. Three assumptions were considered for the mass and energy release to the In the first assumption, only the steam flow from containment durine eflood. To be'::;;;f the SG side of the break was used from the RELAh4 results. 1r3 ' conservative, it was then assumed that all of this dry steam was superhehted to'1300 Stu/lbm (about 5000'F), and the energy release rate was obtained by The actual effluent enthalpy multiplying the steam flow rate by 1300 Stu/lbm. is about 1200 Stu/lba for the first 20 seconds of reflood and gradually decreases to about 600 Btu /lbm after that. Thus, assuming that only dry '
- r-y ,
.1-superheated steam is released is'M conicavative. . .
In the second assumption, the mass and energy flow rdtes 'from '. Se SG side of the break were used, but the energy flow was aug5lented to account for 0 superheating. At 70 psia, saturation is about 310 F, and the specific enthalpy of steam is 1185 Stu/lbm. At this pressure, the specific enthalpy at 0 5000 F is only 1282 Stu/lbm. While the SG tubes are a little below 500 F - at the start of reflood, their temperature is on the order of 350 F at the end of reflood. Therefore, ' adding 100 Stu/lba for each po'und of steam flow is
$ y conservative. The steam flow rate used to calculate this added The additicnal energy was the same as that used in the first assumption.
energy was about 8% of that computed by RELAF4 at the beginning of reflood and about 6% at the end of reflood. I In the third assumption, the mass and energy released from the SG side of the break by RELAF4 were u:ed direct.ly. The licuid phase falls to the pool as
- l
. ;
/ -
I
;j i P
- h y)?.jl f:f ESL10P4 .
h.4 U tifsd D. released. Naturally,- this case results in lower peak temperatures and , pressures than the superhaated-steam-only case, but it is more realistic and it is conservative. , , For all three assu=ptiens, the . release of water from the pump side of the . A I break is ignore'd.- This release is all liquid phase and goes directly to the 9gnf ceJJemu~T %The f~ amount of water in the PM1 has a negligible effect on the ep:" p el . ' c<s,L:,,., ant-The REl.AP4 mode.1 nad to temperature and pressure history of thesvapor regicn. use ICCS water at 3bO O F in order to avoid instabilities, whereas the ECCS weouLY fy water,i.tractualAy witT~be about 100 F. Since the water coming out the pump side of the break will have had no contact with the core and little with any of the metal enclosing the primary system, it should not be significa'ntly-In view of the large difference warmer than when it left the accumulators. between tl[ actual and the model ECCS water temperatures, neglecting the liquid flow frem the pump side of the break is 'Qkkh more realistic than including -- Q, -e it. , 3.5 Ccntainment Results The results of the CONTEMPT runs are shown in figure 3.9 through 3.14. Figures 3.9 and 3.10 show the results for the case where only dry, superheated steam flow from the SG side of the break was considered,' and the eqergy
. release rate during reflood'was obtained by multiplying the steam flow rate by 1300 Stu/lbm (which is approximately the specific enthalpy at 500 F and 70 psia). Figure 3.9 shows the results for Method A and Figure 3.10 shows the results for Method B. The two cases are identical to 120.4 seconds since the
. difference is in how the mass,and energy releases are handled after reflood.
- The figures show that the contain .enti atmosphere reached almost 70 psia and Since only dry 325cF at 84 seconds just before the containment spray began.
steam was released "to the containment during reficod, the centair.mant spray 9 e -
,,?-9 - - - -- ?*y--, , pw-. pwe, 3 yw-,-g g sq 9y> m vp- , , em ..-e ~
il@:# ruiag, f? ij# J {1 . N has an immediate and dramatic cffect on the containm:nt vapor r !gion
~ '
temperature and pressure. ,The peak pressure ,. .- equals the containment design pressure of 69.7 psia, ay t%; : te pe- turc he*p..,. . etm. 3
- :rget m In view of the at. .... b conservative assumption of releasing
[ W. ~ only dry, superheated steam during reflood, this is not considered significant. It is inconceivable that the superheated steam could flow from the steam generator to the break with the saturated water and not mix to form a homogeneous, two-phase flow. Since the Method A assumptions are not suitable for a long-term model, the iun shown in Figure 3.9 was terminated at two hours, while the Method 3 ruri in
- Figure 3.10 was continued to ten days. The results of the two methods are quite close at two hours. The dip in the atmosphere pressure and temperature at 30 minutes (1800 sec) in Method 3 is due to the shutdown of the LPIS at the time when the RWST runs dry. This does not show up in Method A since the -
. primary s'ystem is not modeled. The chang.e in be' at 30 minutes inithe
! Method A result is due to the fact that the source of water for the un7:.m j . a,.ra:...cI 1; p:dr s,u g)he T j vapor ' containment spray changes from the RWST to the warmer 4: ! region temperature reacFes 1350F at abou: 8.08 days (598,400 sec) in Method B (see Figure 3.10). f Figures 3.11 and 3.12 show the results for the release of a two-phase j
- mixture with the energy flow augmented to account for superheating the steam l
i ) fraction. Feak pressure is about twozy;*p psi below the design pressure, and the j t o.t a w r a y 4 ./a ,;e, Behavior peak 3 temperature is -j=st about s(Et:Q:d W = , w +c. l l af ter a few hu.ndred seconds is nearly identical for all the A cases and all J t . the S cases. This is to be expected since events are dominated by the
)
- The i
absorptive capacity of the heat structures and the effect of the sprays. ,
. e Te.i.. p atmospheric temperature reaches 135 F at about 5 de:ys.
4 15-p e , , , , - - - p .- ,,--.-.m ,,.>.%-.e -ya e-.,*
- raua
. l
.lf'iLic:aaQi 1.Ch i r'4 hk!$kEdh In view of all the conservative assumptions made ellewhere, the results shown in Figures 3.11 and 3.12 are sufficiently conservative and meet the Standard Review Plan requirement for superheated' steam. Since the effluent to t.he containment will certainly not be dry steam in view of the ' carryover rate
-w.
fraction in the core, this assumption of wet steam with the steam fraction arbitrarily superheated appears to be the maximum which can be justified as realistic. ' Figures 3.13 and 3.14 show the results when the RELAP4 calculated releases ' u.LZ d49 any energy t, aeraunt saparima%g s. tea.
. from the SG side of the breaQ" a%4-unchanged-4nto CONT %for the rel u E*
dI" 9 ;tl"* Peak pressure was over 4 psi below the design press,ure, and g reflood period. F. t A a ce 4 4tmso4uk. ,),y s the peakjtemperItbr .was .we-than y*hh the d::'p t-9= _. ;;r: 'The 0
,Jg,. -ed atmospheric temperature dropped to 135 F after about 8 days. So many
^ conservatisms, including the use of 300 F0 ECCS watar, were made in arriving, at the releases to th=A>4.d~r..~si1 dut ing reflood_,and post-reflood g t. anhese u.wc w - -
1 results are definitely conservative., ,T'ney doMmeet the SRP mandate for superheated steam,._h-A.' ... . 4.0 Secondary System Pioe Break Analyses of the containment response to a. secondary system pipe break were
. also made. For P'n'R's the mos't limiting break location is a main steam line break with pure steam blowd'own. In the case of Palisades the results show that a single failure assumption which allcws both steam generators to bicwdown will produce peak pressures and temperaturs which exceed design The model and assumptions that were used in analyzing the main steam
. v alues .
line break are given in the following discussion.
,e =
WQ sJhwd d 4'.1 Assumptions , A main steam line break (MSLS) analysis was perf'ormed'by' Consum Company.1 Results given in this reference are used for enaparisen E.h .se data for the full pcwer MSLB purposes. In particular, mass and energy 1., case discussed in the Palisadas FSAR i,s provided in Table 1 of. referen f The Palisade,s FSAR full power analysis assumed: A double-ended guillotine rupture of a main steam line inside the (1) containment. (2) A reduction in feedwater flow from fuli flow to zero o seconds immediately following scram at le'ss than 2 seconds containment pressure: Both main steam isolation valves would close on icw steam gen (3) lt pressure (500 psia) causing the unruptured steam genera in eight seconds. ' M
..c Off-site power was available. %
(4) ' (5) Only two containment spray pumps war'e available; no air ecc avail able. Fure steam blowdown (no moisture carryover). (6) (7) A highly conservative containment heat transfer model. In addition to the results reported in reference 1, a number of The analyses employed
~
Palisades containment response to the MSL3 were made. i RELAP4 to obtain mass and energy release rates and CONTE centainment response. id
~
The RELAP4 mass and energy release rates were obtained k junction, and one ' !
' model based on one volt.me, one heat conductor, one brea -
3 t 1 Palisades Plant - Automatic Initiatica of Auxiliary 21, 1980Peedwaterletter frca Sy RR, Palisade's Plant, Decket 50-255-License DFR-Nuclear Regulatory Commission. PO e
L 3EjbhN$kh MdiFM li Two break sizes and three ft edwater flew assumptiens ' feedwater fill junction. were analyzed. The resulting break flow rates are su:=arized and compared to For'the RELAP4 analyses, the reference 1 results in Figures 4.1 and 4.2.. steam generators. were assumed to be at 770 psia, with an average water . l g._ I enthalpy of 552.2 Stu/lbm and 'ccatain 128,456 lbm each. The primary system was assumed to be held constant during the blowdown with 513.83cF local 2 temperature and a 952 Stu/hr/f t joF heat transfer coefficient in the steam l generator. Figures 4.1 and 4.2 show that the main effect cf the feedwater is to prolong the time of blowdown period and increas.e the total mass and en to the containm'ent. ~ The containn'.ent responses for a number of MSLS cases have been com The results are given in the following discussion. 4.2 Centainment Resconse Results . .
.c
-- m Case 1 The first case selected for analysis was intended to determine if the .
l CONTEMPT-LT/028 model used would give result.s similar to those Ccnsequently, two CONTD'?T runs were if similar assumptions were e ployed. These CONTEMPT 1
- made, using the reference 1 mass and energy release rates.
f runs assumed two spray pumps and one f an cooler were available and eight seconds for the CONTEMPT Tagami/Uchida heat transfer corr ' l The one run assumed that off-site pcwer was not available so the two spr The other CONTEMPT run assumed off-site pumps were started .at 84 seccnds. l I power was available so the spray pumps were started at 30 seconds. The containment histories.for the two Case 1 runs are ccmpared to th The ecmparison between the reference 1 pressure histcry in Figure 4.3P. is close, results with spray after 30 seconds and thegreference 1 results ec.:ta,:.. indicating an acceptable CC" TEMPT modeT. The,,tamperature' hi CA.C2. I;.;L are shown in Figures 4.374 and 4.3T-5. - C?J ' -1S- ..
._ .- , , . - - - + , , - ,- ,e-~
,- ,, ~y , ,n,,
. ,7.c -?
. t r. : a
, M !i
^
- s. My; u Case 2 . . . .
The purpose of the Case 2 analysis was to determine if, the one volume RELAP4 model was adequate for obta;ining mass and' energy release rates to the containment. The blowdown mass and energy release rates for various feedwater and break 'ar'en bombinations have been 'noted in Figures 4.1 and 4.2 For Case 2. l the ruptured steam generator blowdown was simulated by the 36-inch break I (area = 6.12.f t2) with main feedwater only. This feedwater flow was The initially 1650 lb/sec and ramped down to zero flow at 60 seconds. l unruptured steam generator was assumed to isolate ,(MSIV closure, not failure) The " mass so the mass and e'nergy release rates were obtained from refrence 1. and energy release rates for the two steam generators were added for input to. the CONTEMPT model. ! The CONTEMPT assumptions for Case 2 were similar to the assumptions for the Case 1 run with spray after a 30 second delay. The containment , M pressure l and temperature response from. Case 2 is shoEn[NFigures 4.4P and 4dT, . respectively. The peak pressure is about 65 psia, which is slightly less thar for the comparable Case 1 run and the reference 1 value. Therefore, the one I volume RELAP4 model was judged to be adequate for obtaining mass and energy release rates. It is noted that complete phase separation is modeled in the RELAP4 analyses so that pure steam blowdown oc.urs. Case 3 Cases 1 and 2 established that the CONTEMPT and RELAP4 models were adequate for obtaining contaidment response to a KSLB. Cases 3 and 4 were i l designed to determine the response of the Palisades containment to the MSL3 l for blowdown of both steam generators, with off-site pcwer availab'le. Case I 1
- ;
I assumed that'each steam generator would blow down through a 24-inch break 1 (3.C6 ft2 ). Case 4 assumed that the ruptured steam generator would blow l
\ ' ' I! 2 E h)951fdIIb5b $ doven through the 36-inch (6.12 f t2 ) break and the unruptured stea . gentrator would blow down through a 24-inch break. , The assumptions used for Case 3 include: , (1) If off-site power is available, the spray pu=ps will be activated at
- ( '
30 seeinds after high containment pressure (5 psig). High containment pressure occurs in about 1.7 seconds. A conservative . value of 33 seconds was used in the analysis. (2) Single f ailure is the Main Steam Isolation Valve (P.SIV) failure ! causing both steam generators to blow down. l (3) Ruptured steam generator blows down through one-half the maximum areas, or 3.06 f t2, as areas larger than this would not give a pure steam blowdown. (4) Isolated steam generator blows down through one-half the steam-line 2 area becuase of MSIV flow area restrictions, thus through 3.06 f t , (5) All three spray pumps and all four-fan'wolers will be ava,il'able. The single failure is assumed in the MSIV. (6) The CONTEMPT time TpEAT, for the Tagami/Uchida heat transfer correlation was changed to 99 seconds to correspond with tne end of 1 blowdown. (7) Main feedwater is available to each steam generator at 1650 lb/sec l l initially and ramps down to zero' flow at 60 sec. i The resulting containment pressure and te perature history is shown in j
Figures 4.5P and 4.5T, respectively. The peak pressure is about 107 psia, which is substantially greater than the 55 psig design pressure. 0 l l -
T.>t2 A F T The results show that the worst single failure assumption is a MSIV failure which would allow both steam generators to blowdown. This is - possible since the closure of Palisades MSIVs is only in the forward direction due to the nature of the MSIVs (check valves held open by air against the normal flow of steam). This makes it possible for a steam line break.to give rise to the blowdown of its associated steam generator plus the blowdown of the second steam generator through the failed MSIV,- connecting header, and reversed flow through the closed MSIV. This produces the maximum pressure and temperatures which are higher than. I design values. t . l Case 4 The assumptions used for Cas~e 4 were identical to those used in Case 3 except that the ruptured steam generator was allowed to blowdown thrc:;gh the ! maximn area of 5.12 f t2 . The resulting containment pressure and j temperature predictions are shown in Figures 4.6P and 4.5T, respective! / . The peak pressure is about 106 psia. f Case 5 Cases 3 and 4 assumed that off-site p5wer was available. Case 5 was run to investigate the containment response for the loss of off-site power assumption. Case 5 is similar to Cases 3 and 4 except for two assumptiens.
First, because off-site power is lost, the spray pumps are not available until t c4 seconds. In addition, the loss of off-site power results in a complet'e' and l l immediate loss of feedwater. , 1 l l .. l - l l . . 1 -
~
-3/=
l l l
1D 1L as F'T l Case 5 was based on each steam generator blowing down through a 24-inch I di ameter, break. The pressure and temperature response is shown in- . \ i Figures 4.7P and 4.7T, respectively. The ". peak pressure
'M is about'98 psia
- 2'
\ % : m e e.b e h a le- 0 ~ 'N, peak3 temperature of 465 F at 10 seconds. ! l C.ase G _ i Analyses have also been. performed assuming a fix which would prev In this case the single fai-lure the blowdown of both- steam generators. assumption is loss-of-offsite power with a failure of one diesel The mass and energy release data used in the analysis is for generator. This is discussed the full power MSLB with one steam generator bloddown. '
- u. t by Consumer Power Company in ref.1 and provided in Tab 1e d
( assumptions made in the mass and energy release analysis are the following: 1. A double-ended guillotine rupture of a main steam line inside the containment.
- 2. A reduction in feedwater flow from full flow to zero ove l
1 seconds innediately following scrmn at less than 2 seconds on
;
1 ' high containment pressure. /
- :t: -
l
. - . . _ . ._ _. _ _ _ _ _ _ _ _ . . - - ~ . . . _ . . - _ . . . _ - . ___ ._ , -.
. VRA~T
- 3. Both mains' team isolation valves would close on-lcw steam generator pressure (500 psia) causing the unrupture stea=
generator to isolate in eight seconds. I'
- 4. Off-s.ite power was available to maximize the rate of energy transfer. from the primary to secondary.
- 5. Pure steam blowdow'n (no moisture carryover).
For the containment response calculation the following assumptions were made:
- 1. Loss-of-offsite power and f ailure of oni diesel cenerator. .
- 2. 2 of 3 containment. spray pumps available.
~
3. Containment spray initiation at 35.7 seconds (200 g;m) and fuil flow at 52~.5 seconds (2650 gpm),[ !? sic't-u 4 :-) . 1 of ? air coolers available at 23 seconds. 4.
- 5. Tagami/Uchida heat transfer correlition ~ ~% with Tagami peiGme _at - *~
end of blowdown (63 seconds). ^
- The results of this analysis are the pressure and temperature u.2 P u.L T responses shown in Figures f and F The calculated peak pressure is 65.5 This is 1.2 psi below design. The psia reached at 67 seconds.
Therefore,
' calculated peak temperature is 413 F reached at 37 sectads.
e based en this analysis, a fix which would prevent the blowd:wn of both , steam generators would limit the calculated peak pressure to 1.2 psia below design. l'cJ isulo s. f t an1- - frapend %Lm'ed Sraufiu%n s '
' c. de b ert Q ra.y 1 J i<M a c.Lorp rzelnyreci b v en - w , ^/ow'h r 2%
Tim e , v ackr so.s.n Lic.en sa gett r b- D. P. W a h e o f d e,nsu-crs Per
,es, Co. 6 D. Cmt,1 & Id = f M Rc .
r
- Aj- '.
e* .e- * " @ em 4 .ese wm- ,- - - - - y- ,,e w a- ,w-w :---,.,,---r- -- - - - - - - - . . . , - - a w- -e.v,, ,e -- - ~~ , - - , - , - - _ - ~ e- -
---mw--
i 1
- 1
~ ' I k4 bl Conclusion - Based on the results of Case 1 and 2, the CONTEMPT and RELAP4 models are The results of Cases adequate for obtaining containment response to a MSLB. 3, 4, and 5 showed that the blowdown of both steam generator will result in This is containment pressure a-d tere"'"-er "'% exceed design values. i re s44 of h ; regardless of whether off-site power is available.
, p S Lowu' d s.T a elssl y e. G a y d.L arssle( q <evany & b),we}n.,,
' *4 5*e m y - mfors wo41 4,9 A c N . e r 9e d p m ure
~' " & oleuy G d. .
O e 5 e
"em t 4. - ;
e= 9 y , -
,-=-g y--- ---yy-, .,m-y - , - , , ,, , .- .-, ,.-.w.-,
y w,,,,vg-,,,n.-
4
. Table 3.1 Palisades Double-Ended Suction Leg Srea'(# Gum
*
- Q} &l ~1f:e f NQP7 Ci c Blowdown Energy Balance -
(Million Stu) 1-- 0 Seconds Decrease 20.4 Seconds Primary System Coolant Inventory 253.7 246.6 7.1 Steam Generater Coolant Inventory 140.0 2.0 138.0 Secondary Flow to Turbine (l) -- -9.2 -- Accumulator System Inventcry I2) 19.5 0.7 18.8
- Core Stored Heat 18.9 - 4.5 14.3 Conductor Stored Heat (3) 111.0 3.7 ,107 3 5.0 Decay and Fission Heat -- --
O 543.1 253.4 285.5 Note: , .
~y
. : r-: -
(1) Flow continues until valuve is fully closed at six seconds af ter the break. Energy value is net loss for steam and feedwater flows. (2) Accumulators and lines at 900F. (3) Conductors include all metal transferring heat to the primary coolant systein except for the fuel rods. e e e O 22- ', O e w ,-wq. -g- . 5- , . -u--r- e. - - e -e-* - .wn.= .w%-_y<--
---,----<w w we
- 3 ---e --w -
<-v-y6 % -
v- -
Table 3.2 ; fl [?";f"
~
-- t
~*
Palisades Double-Ended Suction Leg Break I b'yCs U. Reflood Energy Balance
. , (Million Stu) -
t 1-- 20 Seconds Decrease 120 Seconds Reactor Coolant System Inventory 22.4 -3.1 25.5 Safety Injection Tank Water (1) 77.6 -- Safety Infection Pump Flow (1) -- 13.5 -- Core Stored Heat (2) 16.2 11.0 5.2 Decay and Fission Heat -- - 12.3 -- Primary Vessel Walls 59.3 3.3 Sd . b '.
~
Primary Vessel Internals 12.4 3.5 - 8.9 1.0 27.4
~
Primary Loop Metal 28.4 Steam Generator Inventor- 137.9 33.7 104.2 (I. L. 69.8 - 59.1 = 10.7)(3) Steam Generator Tube Metal . 14.3 3.6 -
. 10.7
~
,, 7,, ,, .
~
. (I.L.' 7.6 - 6.3'= 1'.1)(3) r
~
TOTSLS . 290.9 156.4 237.9 l . j . . . Approximate Break Flow Energy , S.G. Side 72 (106) Btu Pump Side 81 (106) Btu i l Total 153 (106) Stu Reference Temperature is 32cF Notes: (1) The S.I. water temperature was 3000F to prevent numerical instabilties. Actual value should be 1100F. (2) Based on ANS + 20% decay heat curve. (3) Energy frcm intact loop steam generator. , v
,g -
,r,-e-,, -y ,,----r- , p-ww-p w y- -,yw-. ,e- gew ,, -,y y gww w- e--- 4 -,-
~
f 7g' Table 3.3 ?N.t 3 @y N.i:fhE ;:. 3 Heat Structures in Palisades Containment Model I Meucture Are a f t 2 Thickness ft
- i. e.
- 1. Tanks and piping (.453 inch) 19,332 .0378
- 2. Ducts (.10 inch) 20,072 .0083
- 3. Reacter crane (2.35 inch) 6,973 .1958
- 4. Internal concrete (33 inch) 9,401 . 2.75*
- 5. Gratings and trusses 20,996 .0144
~
- 6. Containment, dome '7,270 3.0217
- 7. Containment dome base . 11,000 7.75
- 8. Containment side wall 50,600 ~ 3.5217
- 9. Storage pool floor'and shielded walls 4,456 4.35
- 10. Containment base slab 8,229 12.44
- 11. Biological shield all 2,340 7.8672
- 12. Structural support steel .- 26,320
* ~
." % .45
,, ~;?'
- Deck received had 2.25, which was in errer.
O i . 7 : C
-2.4 - -
_ . . - _ _ . _ _ _ ~
n p y .,u ilr:x 1 table 3.4 1 3
. . . M* b.<:U'd
.3 4 4
Palisades Centainment - Initial Conditiens . Outside air temperature 950F dutsideairpressure 14'.7 psia
~
- b. %. ~
Relative humidity of outside air 0.60 Volu.ne of primary capable of holding liquid , 3050.3 f t3 Temperature of primary system vapor region 2500F ' Temperature of primary system liquid region 2500F Volume of eywc41 codiwmed . 1.6ES f t3 r Voline of 1iquid pool on., ,c.-sin-.st' 7,;d 1 ocr %%I 10 ft3
- e. stang .
Temperature of d=y.41.1 vapor region 1200F ..- e.nwsmr Temperature of d=;uo.14 liquid region 1200F . Pressure in 4;:yrre+1 cent lammf 14.7 psia Relative h.midity in 9.weJ! c4 Mmc # 1.0 Horizontal cross-sectional area of d=ywei-1 8,229 f t 2 ce medamc.nf .
*N __
..% ,;.
. p l
6 l l . l . l 8 , 1 v - l - 1 .
TABLE & y* ,
- 3 (E /4 F '{
. Main Steam Line Ercak Mass / Energy Release Data ...
Ruotured steam Generator Time - (Sec) Lbm/hr Stu/Lbm
- 1 0.0 3.266E07 1200.7 .
; ~ . 0.1 3.266 E07 1200.8 0.2 3.186 E07 1201.2 0.3 3.106 E07 1201.5 0.4 3.037 E07 ' 1202.0 0.5 2.957E07 1202.3 O.7 2.826E07 1202.8 1.0 2.637 E07 1203.5 1.3 2.501E07 1204.0 1.5 2.409 E07 1204.3 1.8 2.283 E07 1204.5 2.0 2.215 E07 1204.6 -
2.5 2.057 E07 1204.8
. 3.0 1.942E07 1204.8 4.0 1.759 E07 1204.5 -
5.0 1.621E07 1204.1 7.2 1.370E07 1203.2 8.0 1.336 E07 1202.9 10.9 1.233 E07 1202.3 15.0 1.062 E07 1200.9 . 20.0 9.592 E07 1199.9 ,~ 30.0 8.221E06 - 1137.6 L - 40.0 7.193 E05 119T*.~0 45.0 6.852E06 1195.1 50.0 6.266E06 1194.1 '. 54.0 6.2SOE05 1193.5 ' 60.0 5.938E05 1191.1 68.0 5.481E05 1191.1 63.0 0.0 [
. Isolated steam Generator -
Time (Sec) Lbm/hr Stu/Lbm 0.0 1.656E07 1200.4 0.1 1.656 E07 1200.4 0.2 '1.656E07 1200.6 0.6 - 1.587 E07 1201.3 1.0 1.530E07 1201.8 1.3 1.496 E07 1202.2 l 1.5 1.473E07 1202.5 l 2.0 1.416 E07 1202.9 l 3.0 1.279 E07 1203.6 . ! - 3.5 1.233E07 1203.8 ' 4.0 1.153 E07 1204.0 ~ 5.0 9.930ECS 1204.2 5.4 9.135ECS 1204.2 l 6.0 7.650E06 1204.3 6.4 6.622E05 .- 1204.2 6.8 5.709E06 1204.2
- 7.2 4.339E05 1204.1 7.8 1.4S4EOS '1203.9 ,
8.1 0.0 , 1203.3 . _,9,
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