ML20072L689
| ML20072L689 | |
| Person / Time | |
|---|---|
| Site: | Grand Gulf, 05000000 |
| Issue date: | 08/31/1982 |
| From: | Gasser R BROOKHAVEN NATIONAL LABORATORY |
| To: | NRC |
| Shared Package | |
| ML20072L675 | List: |
| References | |
| CON-FIN-A-3399, FOIA-83-81 NUDOCS 8303310476 | |
| Download: ML20072L689 (467) | |
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{{#Wiki_filter:_ 4 BNL-NUREG- . . INFORMAL REPORT
,33 LIMITED DISTRIBUTION
.J l ifri ANALYSIS OF FULL CORE MELTDOWN ACCIDENTS IN THE GRAND GULF REACTOR PLANT
- R. D. Gasser Department of Nuclear Energy .
jf,) Brookhaven National Laboratory Upton, New York 11973 August 1982 t
- This work was carried out under the auspices of the U. S. Nuclear Regulatory Commission, k ,
B303310476 830224 1 PDR FOIA HIATT83-81 PDR _,~,
ABSTRACT
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A four volume MARCH code BWR model was employed to analyze a selected set of core meltdown accident sequences in the Grand Gulf Unit #1 Boiling Water Reactor. Three basic. categories were considered; namely, loss of containment heat removal, loss of primary system coolant makeup, and failure of the reac-tor protection systems. Particular attention was given to the production, disposition, and combustion of hydrogen in the containment building. The re-sults of the analysis indicate a potential for severe hydrogen burns-ar.d/or local detonations. . e
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i TABLE OF CONTENTS Page 1:2)) A8STRACT. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . . iii i
1.0 INTRODUCTION
. . . . . . . . . . . . . . . . . . . . . . . . . . 1 2.0 LOSS OF CONTAINMENT HEAT SINK. . . . . . . . . . . . . . . . . . 5 2.1 TPW Ac ci d e nt Seq ue n c e . . . . . . . . . . . . . . . . . . . . 5
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- 2.2 TW Accident Sequence. . . . . . . . . . . . . . . . . . . . 8 2.3 S2 W Accident Seque nce . . . . . . . . . . . . . . . . . . . 9 3.0 LOSS OF COOLANT MAKEUP . . . . . . . . . . . . . . . . . . . . . 12.
3.1 TQUV Accident Sequence. . . . . . . . . . . . . . . . . . . 12 3.2 TPQE Accident Sequence. . . . . . . . . . . . . . . . . . . 16 g) 3.3 5 2E Ac ci de nt Se q ue n c e . . . . . . . . . . . . . . . . . . . 18 4.0 LOSS OF REACTOR PROTECTION SYSTEMS . . . . . . . . . . . . . . . 20 4 5.0
SUMMARY
AND CONCLUSION ...............w . . . . 23 , 9 R EF E R E NC E S. . . . . . . . . . . . . . . . . . . . . . . . . . . . . . 24 l l i APPENDIX - GRAPHICAL RESULTS OF MARCH CALCULATIONS. . . . . . . . . . 25
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,- I. INTRODUCTION A preliminary study of core meltdown accidents in the Grand Gulf Boiling Water Reactor (BWR) plant has been completed and the results are discussed in
's. this report. The dominant accident sequences were obtained from the Grand
- $ Gulf Unit #1 studyll3 in the Reactor Safety Study Methodology Applications
, Program (RSSMAP). In that study three general accident categories were iden-
;- tified; (1) loss of heat sink, (2) loss of coolant makeup, and (3) loss of
, reactor protection systems. For the loss of heat sink category, three .acci-dents sequences were identified: TPQI, TQW, and (5,A)I using the nomenclature
; of Reference [1]. In the WASH-1400 nomenclature these correspond to the TPW, TW, and (S,A)W sequences. For the loss of coolant makeup category, an addf--- ,
tional three sequences were delineated, namely, TQUV, TPQE, and (S,A)E which - , have' identical WASH-1400 identifications. Finally for Category' 3, loss of h l reactor protection, the ATWS or TC sequence was considered. These seven acci ' , dent sequences, therefore, make up the body of the present study, The extent to which the accident sequences considered in this report are dominant has not been finally determined. The probabilities assigned in the ll RSSMAP study to some of these sequences (particularly the TPW sequence) have : ^[ been called into question.L2] It was concludedL2] that failure to account for the heat removal capacity of the main condenser in the Power Conversion System (PCS), the functioning of non-safety grade equipment, the additional
, heat capacity of the spent fuel pool and water injected from outside sources o Ji - into the suppression pool has resulted in overly conservative estimates of the l probabilities for the most dominant accident scenarios. Inclusion of the l rs l probability of the availability of the PCS, for example, may reducell3 the
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probability- for the TPW sequence by 10-2 These observations are well taken. Adjustment of the probabilities may result in some accident sequences ,. . S
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being less dominant and necessitate consideration of other accident sequences, which may be more dominant or at least comparable to the ones considered here. When a consensus is achieved in this matter, consideration of additional acci- t 1-dent sequences may be required. However, the present preliminary analysis, will consider only those sequences identified in Reference [,1]. It should be restated, as in previous reportsl3:43 on BWR safety stud-f es, that there are a number of problems associated with employing the MARCH code tolu model boiling water reactors. It is not necessary to reiterate
.D these problems here. There is, however, a code related problem that has not been previously identified which is of particular concern in this analysis.
This problem relates to . inaccuracies generated when hydrogen combustion occurs , in a system in which more than one containment volume is modeled. Because of the BWR de~ sign it is necessary to use at least two volumes; to adequately model a BWR (wetwell and drywell). The intercompartment transfer modeling in the MARCH code can interfere with the H2 burning model and transfer from the cell in which the burn is occurring quantities of H 2 that'should have been consumed during combustion. The result is that quantities of hydrogen can be both transferred to another cell and burned in the same cell. When this oc-curs, a negative hydrogen mass is calculated in the cell. It has been deter-mir.edL6] that inaccuracy in the peak hydrogen burn pressures on the order of M 9". can result from this problem. Because of the scrubbing capacity of the suppression pool inherent in the
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BWR MARK III containment design, any potential for bypassing the suppression
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. . 'T pool could have an important impact on consequences. The integrity of the-drywell wall is crucial to maintain the integrity of the suppression pool and its decantamination capability. However, a hydrogen detonation of sufficient magnitude occurring in the space directly above the suppressica pool may be able to generate pressures sufficient to rupture both the containment struc-ture and the drywell wall. A mechanism has been postulated wherein a hydrogen burn in one containment volume both raises the overall' containment ' pressure and also serves as a triggering mechanism for a detonation in an adjacent vol-ume. The potential for this type of sequence in fact may exist in the volumes adjacent .to the drywell wall just above the suppression pool. As hydrogen bubbles through the pool, its concentrations will be highest in the area above the pool and less as it diffuses upward into more elevated sections of the containment structure. The presence of electrical equipment at higher elevc-n tions, therefore, may create the condition described above in which a H2
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-) burn at a higher elevation coald trigger a detonation at a lower elevation with perhaps sufficient force to breach both containment and drywell walls.
With this scenario in mind, a four cell MARCH nodel has been employed in this study with a view to establishing what sort of H2 concentration distribution l may be possible in the Grand Gulf containment building. Hydrogen bubbling ;4 s l through the pool enters the wetwell atmosphere and is transmitted according to
. the MARCH intercompartment transfer model to two additional volumes, each suc-cessively at higher elevation in the containment building. All four volumes are connected in a linear manner such that volume #1 (drywell) is connected to volume #2 (wetwell) which is connected to. volume #3, etc. (1 to 3,1 to 4, 2 [
to 4 flow paths are disallowed). In all the cases reported here, it has been assumed that 75". of the clad
.~, is reacted when the core slumps onto the lower vessel head. In addition, all
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. hydrogen burns are assumed to. commence at an 8% volume . fraction of H2 and terminate at a 4% volume fraction. Due to lack of information regarding the .
t . l type of concrete used in the reactor cavity, the default concrete in the MARCH code has been used throughout. 9 5 4 5 f . 4 1 4
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- 2. LOSS OF CONTAINMENT HEAT SINK s~
In the Grand Gulf plant, containment cooling may be accomplished by uti-l 11 zing the Residual Heat Removal (RHR) System in two separate operating modes. In the first mode, water is pumped from the suppressio.n pool, passed through the RHR heat exchanger, and discharged back into the suppression pool. In the second mode, rather than discharging the cooled water back into the ' pool, it is directed into the containment spray headers. In the loss-of-containment-heat-sink scenario, the RHR system effectiveness is lost either by failure of the RHR pumps or by loss of the Standby Service Water System (SSWS) which is necessary to remove heat from the secondary side of the
! RHR heat exchangers. Thus, both modes of containment heat removal (CHR) are assumed to be lost in this accident sequence. The three accidents considered here for the loss of CHR are TPW, TW, and 5 W- 2 -
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2.1 TPW Accident Seouence This scenario corresponds to that of the TPQI in the RSSMAPE13 document. The sequence is characterized by a transient event, which is followed by a ,' failure of one safety relief valve (SRV) in a " stuck open" configuration, to-
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gether with a failure of the CHRS. It is further assumed in this scenario - I that the PCS (Power Conversion System), operating in the mode which bypasses the turbine and feeds steam directly into the condensor, is also not available (Q and W in the accident sequence nomenclature corresponding to a failure to remove residual decay heat). Adequate makeup of primary system inventory is , initially available in the fonn of RCIC, LPCS, LPCI, or HPCS. In this study ! j. the arbitrary choice was made to use the HPCS (High Pressure Core Spray) l l k
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3 rather than actuating the ADS (Automatic Depressurization System) and utili-zing the LPCS (Low Pressure Core Spray) or LPCI (Low Pressure Coolant . Injection). Three MARCH cases were performed for the TPW sequence. LIn the first-(case GG1PW1) the HPCS system is assumed to fail in the recirculation mode when the pumps begin to cavitate (suppression pool temperature approaches
. boiling temperature). In the second case (GGTPW2), no such failure is as-sumed. The third case (GGTPW3) is identical to case GGTPW1 except that the
, RCB is failed when the' pressure reaches 50 psia. The results for these cases'
; and the remaining cases in this report are given in graphical form in Appendix A. The cases are identified by the case numbers designated in' the text. Note that, although the temperature and.other cell conditions are shown for each of the. four volumes, only one of the cells has a pressure plot (usually volume 4 which is the RCB). This is because MARCH constrains connected volumes to be in pressure equilibrium and, therefore, the pressures in all' four cells are Ifh identical.
The HPCS system is able to maintain the core in a flooded configuration in case GGTPW1 until the attempt is made to go to recirculation. Since the
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CHRS is inoperative, the pool temperature has already exceeded 200 0 F (recir-culation mode failure criterion) by the time (700 min) that the recirculation system is called up'on t'a function and recirculation is, therefore, not estab-lished. . The core is subsequently uncovered with the accompanying production of hydrogen. A hydrogen burn occurs in volume 2 (volume containing the sup-pression pool) at about 850 minutes and a second burn occurs at 900 minutes in
,j volume 4 (RCB). Both of the H2 burns produce pressures on the oraer of 90 I
] psia. Even considering the conservatism due to the modeling problem v
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- i identified above, these pressures would seriously challenge the integrity of
% the.RCB. The subsequent pressurization for this case is characteristic of
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that produced by the steam and non-condensibles generated during the melting attack of core debris on concrete. Thus, in'the absence of RCB failure by H2 burning, the pressure is predicted to exceed 90 psia by 25 hours. 4 Case GGTPW2 does not fail ECC in recirculation,'does not uncover the core, and, therefore, does not generate hydrogen or H2 burns. In addition, I the vessel is not breached with the result that there is an absence of core debris attack on concrete. A gradual pressure increase due to steam occurs in containment due to the lack of CHR capability and the pressure increases at a rate of about 2 psi /hr afdr 500 minutes. In case GGTPW3 the containment ,is assumed to fail at 50 psia. Since the ECC is also assumed to fail in this case, a similar H2 burn to case GGTPW1. occurs. In fact, this first H2 burn exceeds 50 psia and hence fails the RCB. The failure of containment does not, however, prevent the second.H2 ! l $ l burn which now occurs in volume 3 rather than volume 4. However, the peak , j pressure during the burn is partially mitigated by the failed RCB. Although the mole fraction of H2 remains high in the RCB (in excess of 20". after 24 t
. hours) the oxygen concentration is depleted both by the H2 burns and purging :
. out of the system during and subsequent to containment failure. The result is i that no further H2 burns occur. '
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F 1. 2.2 TW Accident Secuence
- This scenario is identical to the TPW accidenti except that the SRV's are , . . _
assumed to operate normally, opening at the prescribed set point and properly re-seating. However, in the absence of residual decay heat removal, the nor-I mal operation of the SRV's will pressurize the RCB. In case GGTW1, this scenario is treated with the stipulation that the ECC , pumps fail in recirculation when the suppression pool conditions result in l pump cavitation. The results of this case are not significantly different from case GGTPW1 with the excep' tion that without a " stuck open" SRV, the pre-sent case does not lose primary system inventory as rapidly so that the con-densate storage tank inventory lasts about 100 minutes longer (300 minutes).
- i. When the attempt is made to go to recirculation, however, the suppression pool has already reacfied saturation so that the pumps fail immediately due to cavi-t tation. As in the corresponding TPW case, the core uncovers soon after loss i
! of ECC and two separate H2 burns result in compartments 2 and 4 as before. ( ( Cases GGTW1 and GGTPWI are quite similar except that the timing of major l~ events is shifted by about 100 minutes. As in the TPW case, the H2 concen-trations in all 4 compartments exceed 20% even after the second H2 burn, b'ut i the oxygen concentration is below the required level (6%) for combustion. The peak pressures in this case are on the order of 95 psia and still increasing at 2000 minutes. A TW case was run assuming that the ECC pumps do not fail by cavitation and continue to deliver their rated flow. Case GGTW2 represents this sce-nario. This case is similar to case GGTPW2 except that recirculation is es-tablished about 100 minutes later than in the TPW scenario due to the lower rate of primary system inventory loss. Because the cote is not uncovered in g
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the time frame considered, there is no H2 production and no H2 burns. The
% pres.surization rate is similar to GGTPW2 but the shift in time results in
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pressures that are nearly 10 psi lower than those in the GGTPW2 case. A third case was run for the TW scenario with the same configuration as case GGTW1 but with containment failure and blowdown occurring when the RCB pressure reached 50 psia. The results for this case are identified as GGTW3. Again, this case is similar to the corresponding TPW scenario with the excep-tion that the timing of events is retarded. 2.3 SpW Accident Secuence This accident sequence was selected out of the set of sequences, (S,A)W identified in Reference 1. The selection was arbitrary and future analysis will consider larger breaks as denoted by the S and A sequences. In the ac - cident scenario considered here, a 1-inch diameter hnle is assumed to be opened in a steam line. The PCS and the CHRS are both assumed to be failed or, unavailable, but the HPCS is operating initially in the injection mode. As in the TW and TPW sequences, three cases are run for the S2 W scenario; one in which the ECC pumps fail in recirculation (case GGS2WI); a case in which re-circulation is successfully established (case GGS2W2); and finally a case in which the containment fails at 50 psia (case GGS2W3). ! Due to a problem associated with the MARCH code modeling, it is not nre-
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sently possible to vent the pipe break flow into one cell and the SRV flow l . l into another. Therefore, for this sequence, the pipe break is specified to occur in volume 1, the drywell. As a result, the SRV's are also required to l i discharge into the drywell rather than into the suppression pool. It is rec-ognized that this is physically incorrect, but at present it is the only way '
..g the sequence can be treated.
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Reference to the graphs for case GGS2W1 reveals a severe pressure " spike" which occurs at about 950 minutes and reaches about 130 psia. This is not the result of a single H2 burn (between the limits of 8% and 4%) but rather the result of multiple burns. A small burn occurs in compartment 3, which com-pounds the' severity of 2 later burns in compartment 4. The ECC fails in re-circulation at about 770 minutes. Since all the steam from the break, as well as the SRV's was vented into the' drywell, the non-condensibles in the drywell are purged into the wetwell. The wetwell (cell #2) is steam inerted at the time that hydrogen begins entering the system, and by the time it reaches 8% H2 the oxygen has also been purged into cells 3 and 4. When steam flow from the vessel is terminated at about 950 minutes, condensation in cell 3 reduces the steam concentration down below 50% thus de-inerting that cell. At this point the H2 concentration in cell 3 is about 30%. Fortunately, cell 3 has - also been purged of most of its.02 content so that only a small H2 burn occurs, raising the pressure to 65 psia. The increase in the cell 3 pressure 7
-drives additional hydrogen into cell 4, which has the highest e _..1 concen-
[ tration. The two successive 2H burns that subsequently occur in cell 4 (RCB) drive the pressure to $100 psia and then to S130 psia. The importance of coupled effects between local compartmentalized hydro-gen burns or detonations is illustrated by this example. Loss of ECC flow to-gether with condensation and. purging effects can combine, depending on the ac-l cident scenario, to initiate severe hydrogen burns, which may lead to' detonations. i
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'The S2 W case in which ECC is not failed in recirculation is shown in
-h ' the . graphs labeled GGS2W2. This case is similar again to the GGTPW2 and GGTW2
.y cases where ECC was not failed in recirculation. These cases are all charac-terized by lac.6 of H2 combustion and a steady increase in containment pres-sure as steam enters the "uncooled" containment. As in the other two cases the containment pressurization rate proceeds at about 2 psi /hr. At 2000 min-utes the pressure is 460 psia.
For the containment failure case (GGS2W3) the initial H2 burn at 933 .. h-minutes fails the containment and thus purges the oxygen. The result is that i the H2 burns, which occurred in the non-failed case at.about 950 minutes, 'do not occur in this case. The purging of most of the oxygen from cells 1, 2, and 3 during ECC operation, results in most of the 02 being in cell 4 When cell 4 blows down to atmosphere (RCS failure), subsequent H2 burns are prevented. I O 6 l r t q '4, g \;lj .
3.0 LOSS OF COOLANT MAKEUP In these accident sequences a total loss of inventory makeup is postula- (D-ted. This implies that the high head systems HPCS and RCIC, as _weil as the low head systems LPCS and LPCI, have all failed. In addition for the two transient cases, (TQUV and TPQE), in order for a severe accident to occur, it must also be assumed that the Power Conversion System (PCS) is unavailable. Although none of the cases in this section specifies a loss of containment heat removal, that condition is also tacitly imp, lied. It can be argued that, if the containment heat removal system is available,' then ECC would also be available since the CHRS and the LPCI both operate off of the RHR system. Thus, if LPCI is not available, then the CHRS is also unavailable. In the strict sense this is not altogether true, since a valve malfunction might al-low use of the RHR for CHRS but not for LPCI, or malfunction of the ADS cculd prevent vessel depressurization and thus eliminate the LPCI system. Multi- . ple failures of this nature will not be considered in this report. ! t 3.1 TOUV Accident Secuence In this sequence the reactor protection system successfully shuts down the reactor, but the PCS is unable to remove the decay heat, and the ECC sys-tems are unable to deliver makeup water. It is assumed that the vessel pres-sure relief system operates normally. Three cases were perfomed in this analysis for the TQUV accident se-quence. In the first case (GGTQUV1) the RCB is not allowed to fail. The sec-and case, (GGTQUV2), is identical to the first case except that the contain-ment is allowed to fail when the pressure reaches 50 psia. The third case, !
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(GGTQt'V3), is identical to case GGTQUV2 with the exception that hydrogen com-s bustion is arbitrarily suppressed in order to assess the degree of hydrogen
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transport between compartments as well as the history of H2 concentration in each compartment.
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The results for the non-failed containment configuration are'shown in the set of plots labeled GGTQUV1. Core uncovering for this case occurs at about 106 minutes, and the core slumps at 142 minutes. Starting at 125 minutes, a complicated set of hydrogen burns occur in all four compartments. In cells .,. 2, 3 and 4, which have extremely high H2 concentrations (20 to 50%), pres-sures ranging from 40 to 120 psia are generated. the hydrogen burn instabil-1 ity described in the introduction is probably most severe in these extreme cases. Cell temperature during H2 burns approach.60000 F. These extreme temperatures may in part be due to this instability. In all, there were 14 - separate hydrogen burns. Table I shows the time at which each burn occurs as well as the compartment in whic'h it occurred and the peak adiabatic burn pres-sure. In the absence of steam inerting and purging effects due to ECC opera-- tion observed in the loss of heat sink cases (Section 2), the problem of hy-drogen combustion and detonation are particularly severe for this accident i sequence. It is possible that several of the H2 burns could have actually been detonations (particularly burns #7,13, and 14) and perhaps could have resulted in the failure not only o'f th'e containment wall, but -also the drywell wall.
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Table I Peak Pressure 3 Burn # Time Volume # (Adiabatic) 1 125.0 2 38.1 2 127.1 2 73.4 3 132.2 2 59.2 4 133.3 2 46.2 5 137.4 3 40.9 6 137.5 1 44.5 - 7 , 137.6 2/3 123/82.8 8 140.7- 1/2 32.6/76.4 9 140.8 3 39.3 . 10 142.9 2 74.1 11 143.0 1 37.7 { 12 144.1 4 60.1 , 13 144.2 3 172.0 14 154.3 4 129 l-s e l 9 .
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The case shown in the plots labeled GGTQUV2 give the results for the TQUV
' configuration with containment failure imposed at 50 psia. Because contain-ment failure can be specified to occur only in one cell and only on the basis of the total compartment pressure.(not on the adiabatic. hydrogen burn pres-sure), the first 11 H2 burns (see Table I) do not fail the RCB. Case GGTQUV2 is identical to GGTQUV1 until the RCS is failed at 144.3 minutes after burn #13. After RCB failure, the severe burn #14 does not occur. In place of burn #14 in cell 4, three minor burns in cells 2 and 3 occur, none of which ex-ceeds 44 psia. Subsequently, minor hydrogen burns continue to take place at intervals with the.last burn occurring at about 1260 minutes. None of these burns achieved local pressures much above 30 psia but such burns, occurring subsequent to RCS failure, drive into the environment additional quantities of gases and aerosols. -
The final MARCH run in this accident sequence (GGTQUV3) has the same con-figuration as the previous case, GGTQUV2. In this run, however, hydrogen burns are all suppressed by setting the upper burn limit equal to 1.0. the aim was to obtain an estimate of the intercompartment transfer of. hydrogen and the hydrogen concentrations in each compartment without the complica' tion of combustion.- In cell #1 (drywell); the atmosphere is inerted by steam pressure , until about 250 minutes. The oxygen is for the most part purged out of cell
#1 during head failure, so that, although the H2 concentration ranges from l 25% to 10%, a H2 burn cannot be initiated. In cell #2 (cell containing the
! l suppression pool), the atmosphere is never steam inerted and from about 100 to about 1000 minutes the H2 concentration is above the normally accepted deto-nable limits (18%). liowever, to accommodate a detonation for these conditions the oxygen concentration must be on the order of 8%. This condition is met
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in cell 2 for a few minutes just after head failure, again momentarily at about 200 minutes and at 500 minutes. Cell #3, like cell #2, is at no time .,m 2:) steam inerted. The H2 concentration after head failure never drops below b 25%, and subsequent to RCB failure at 500 minutes the oxygen concentration levels out at about 9 to 10%. Clearly a detonation could occur in cell 3 any time after 500 minutes. Finally, in cell 4, the H2 concentration reaches about 35% rapidly after head failure. The oxygen concentration is reduced from 13% at 200 minutes to about 10% at 500 minutes and remains at that level for the duration of the run. Again, a detonation could conceivably occur in cell 4 despite RCB failure at any time subsequent to head failure. ' 3.2 TPOE Accident Secuence The TPQE accident sce'nario is characterized by a transient in which the. decay heat is not removed (failure of PCS). A single SRV fails to reseat and remains in the open position for the duration of the accident. Subsequent ef- , forts to achieve adequate ECC flow for primary system, inventory makeup are { also unsuccessful. The "E" designation, as used in RSSMAP, does not neces-sarily imply total failure of ECC but merely a reduced ECC flow such that the core cannot be maintained in a flooded condition. In this analysis, however, the ECC flow is " reduced" to zero. Thus, the TPQE sequence modeled in this section differs from the TQUV case discussed above only in the assumption of a j.
" failed-open" SRV. Note that the assumption of zero ECC flow may not repre-sent the worst case in this accident sequance. ECC flow which results in a continuous steam flow through the core after uncovery may generate larger quantities of hydrogen if the flow rate is not sufficient to cool the core.
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As for the TQUV sequence,. the same three configurations were rur for this 4 case. Case GGTPQE1 assumes that the containment remains intact, case GGTPQE2
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specifies RCB failure at 50 psia, and case GGlPQE3 is the same as GGTPQE2 ex-cept that the H2 is prevented from burning. Examination of case GGTPQE1 reveals a profile quite similar to case GGTQUV1, the difference being that with a " stuck open" SRV the vessel " blows i down" more rapidly so that core uncovery and vessel failure occur earlier than in the TQUV sequence (126 minutes vs.142 minutes for time-to-core-slump). A large number (above 25) of hydrogen burns occur in cells 1, 2 and 3 from 83 to 130 minutes. The wetwell experiences a H2 burn at about 97 minutes which yields a pressure of 110 psia, and another at 102 minutes (88 psf a). A severe burn occurs in cell #3 at 127 minutes which reaches 154 psia. A final burn in cell 4 (130 min) pressurizes the cell to 67 psia. Comparison of this case - with GGTQUV1 illustrates the fact that the timing of core slump and the rate J
) of core uncovery, (they effect hydrogen generation), may strongly influence the location and extent of hydrogen combustion and/or de.tonation.
The GGTPQE2 case resembles case GGTQUV2 except that core uncovery and vessel failure together with the associated hydrogen burn activity occur ear-lier due to the accelerated primary system depressurization rate. A similar series of hydrogen burns take pl' ace with the first one occurring at 81 ain-utes. The containment is predicted to fail at 127 minutes by a H2 burn in cell #3 that yielded an adiabatic burn pressure of 154 psia in that cell. j Less severe H2 burns continue to about 260 minutes. l The final case in the TPQE sequence, GGTPQE3, was performed in an effort l l- to detennine the relative concentration of hydrogen in the containment in the absence of combustion. In terms of temperature and pressure this run is l l Q V L -. _ k
d *- nearly identical to case GGTQUV3. Because of the increased rate of primary system inventory loss with the " stuck open" SRV in the TPQE scenario, the core is uncovered at about 70 minutes as compared to 100 minutes in the TQUV sce-nario. An inspection of the predicted cell steam, hydrogen and oxygen concen-trations reveals a considerable potential for hydrogen detonation. The tima periods over which detonations may occur is greater than for the GGTQUV3 case. Cell !3 maintains a detonable mixture between 75 and 100 minutes and again briefly at 500 minutes. Cell 3 is detonable from 500 minutes onward, while cell 4 remains detonable from 120 minutes onward. A significant difference, however, is the fact that, with the TQUV case, a detonable mixture exists ir.
, the drywell for about 1 1/2 hours from 130 minutes to 220 minutes. Combina-tion of H 2 burns or detonations in other compartments with a detonation in the drywell could result in cracking and perhaps failure of the drywell wall.
3.3 SpE Accident Seouence The final accident considered under the category, " loss of coolant makeup," is the small break LOCA, S 2E. Similar comments apply to this case as to the TPQE case regarding the degree to which ECC flow is lost. Again, in this analysis it is assumed that a total loss of emergency core cooling capa-
,bility occurs, and that the containment heat removal system is also un avail able.
l Although a large range of pipe break sizes could be assumed in the "S" and "A" categories, only one break size is considered here, namely, a break , which has an effective diameter of 1.0 inch. The break flow characteristics (steam vs. saturated water flow) are also important. Again, for the purposes of this prel_iminary study, the break characteristics were not scoped. The 3 ame
break used in this study was assumed to be located in the steam line at such a s, height that the break flow is pure steam. A break located in a cold leg pipe, l ~
~
. for. example, would be expected to empty the primary system more rapidly re-
+ sulting in core uncovery, hydrogen generation, and core melt-through at ear-lier times.
In terms of the timing of events, the S E 2case should be somewhere be-tween the TPQE and the TQUV cases. In the TQUV case, the SRV's are opened pe-riodically in order to keep the vessel at or.below the pressure set point and, therefore, represents the lowest rate' of inventory loss. The "P" scenario which assumes a " stuck open" SRV and a continuous flow area of 0.14 ft2. rep-resents the largest inventory loss rate. The S2 E with a 1.0 inch diameter break (.005 ft 2) should fall between the two extremes. Two cases were run for this accident sequence, GGS2E1 and GGS2E2. These -
- two cases represent the non-failed and failed containment cases, respectively.
s ...
.) The core is uncovered at about 90 minutes, which is sooner than in the TPQE case (100 minutes) and later than the TQUV case (70 minutes). Multiple H2 burns again occur in both cases, some reaching pressures on the order of 150 psia. Containment failure occurs at about 156 minutes for GGS2E2.
l~ ! I L I 4 i 6
~
_ . .i _ , . ~ _ 7 4 4.0 LOSS OF REACTOR PROTECTION SYSTEMS This accident category contains only a single scenario, the anticipated h' transient without scram (ATWS), TC in WASH-1400 nomanciature. Some of the problems associated with treating this accident with the existing codes are discussed in Reference 2. The MARCH code, of ' course, cannot calculate the os-cillating power profile associated with the ATWS accident scenario. In the event that the recirculation pumps are not tripped within the specified time, power excursions up to 10 times full power may occur. The MARCH modeling for
, the ATWS is necessarily simplictic. The maximum fraction of full operating power is input as a constant, and tha code adjusts the core power level by t
linearly interpolating between the decay heat and a user specified fraction of 4 full power, on the basis of the unswelled water level in the core. . , In the TC sequence considered in this analysis, the recirculation pump is tripped in time to prevent a large power transient. The maximum power level, when the core is completely flooded, is taken to be 16f. of full power.[73 Analysis [8,1] of the BWR ATWS have suggested somewhat higher power levels on the order of 20% to 30% of full power. The lower power level was employed ~ here since it is thought that the FARCH code modeling is conservative with re- ,
. spect to core power. Interpolation on the basis of the unswelled liquid level in the core is conservative since the core will be neutronically shutdown con 1 siderably before the core is completely uncovered. I , i The ATWS is modeled here by setting the upper bound power level to apply at the top of the core (12.5 ft), and the lower bound (decay heat) at the bot-tom of the core (0.0 ft). Makeup water is supplied to the vessel by operation 4
of the HPCS and the RCIC systems. The containment heat removal system, CHRS, , I I _. _ l
_- ~ my m b - ==e-#w* , is also assumed to operate at rated capacity. Both the ECCS and the CHRS are a:sumed to fail when the pumps cavitate (suppression pool temperature ap-proaches the boiling point). The parameter MVMAXS in MARCH is set at 324200 lbs so that the ECCS does not turn on until the water level in the vessel gets down to 13.3 ft or about 10 inches above the core. If ECC were turned on im-mediately, the water level in the core would remain high keeping the power level high and pressurizing the containment more rapidly. Two cases were performed for the TC accident scenario. The first case,
, GGTC1, did not allow containment failure, while the second case, GGTC2, failed the containment at 50 psig. The results for these cases are shown in the graphs labeled GGTC1 and GGTC2. For this scenario, the water level drops.very rapidly until the ECC comes on at about 8 minutes. The water level then con-tinues dropping at a lower rate until the ECC flow just matches the power gen-erated in the partially uncovered core. This occurs when the water level reaches 7.5 feet at about 12 minutes. At this level the core is about 40%
.)
uncovered so that the power is about 10% of full power, and the steam genera-ted from the ECC flow matches the power. This balance is maintained until about 60 minutes when ECC is failed in recirculation due to high suppression I pool water temperature. The CHRS which operates in the recirculation mode was turned ff 6t 40 minutes due to high suppression pool temperature. The CHRS ! which operates off the RHR pumps and heat exchangers can reject 1.74 x 108 l l BTU /hr in the containment heat removal mode. This is only about 1.3% of full power and this system clearly cannot reject the heat generated at 10% full power. The core begins'to slump at about 135 minutes. About one minute later i a massive hydrogen burn takes place in cell #1, which yields an adiabatic burn i pressure of 101 psia. This burn is followed closely by an even more 3
- .Ys m
4 severe burn in cell #4 which experiences an adiabatic burn pressure of 180 psia. This second burn fails the RCB in case GGTC2. These two extreme H 2 .-
'?
burns deplete the H2 concentration in the system so that no further burns -- occur. It is interesting to note that the burn .which occurred in cell #1, the drywell, occurred when the H2 concentration was above 30% and the 02 C0"- centration was at about 10%. It is likely that this would have actually been a detonation that could have been triggered by head failure. l Head failure itself took place at 148.8 minutes so that if ignition of the drywell atmosphere was delayed until head failure, the pressure culse as-sociated with head failure would easily have served as a triggering mechanism for a detonation, which could have the potential for failing the drywell wall. In addition, the H2 burn that occurs in the RCB subsequent to the first burn will fail the RCB and result in a direct pathway from the drywell to the out . i side bypassing the suppression. pool and its decontamination capacity. The timing of the hydrogen burns, head failure and containment building failure events in this particular case seem to maximize the potential for release of-fission products into the environment and, therefore, may represent a worst r case scenario in terms of consequence. 0 l' i l' l A.
,3 .
i. i
~ "
i I 5.0
SUMMARY
AND CONCLUSION i s
/
Tne analysis that has been performed is a preliminary one in'which only a very limited number of accident scenarios have been considered.- No parametric
. studies have been performed, as yet, which might reveal ~ combination of circum-stances or parameters that could produce more severe results. These type of analyses are planned for future studies. Nevertheless, this analysis has de-monstrated the potential problems associated with hydrogen production and com-
, - bustion. It has been shown that for all the accident sequences considered here, the local accumulations of hydrogen will very probably exceed the deto-nation limits. Combinations of steam pre-pressurization with Hy detonations or combinations of H2 burns with R2 detonations may fail not only the con-
- tainment building out also the drywell wall. At least one accident scenario',
the ATWS, has been shown to possess the necessary conditions fo'r a detonable n mixture to occur in the presence of a credible triggering mechanism, namely,
}{} '
, failure of the reactor vessel head. The primary conclusion reached by this L preliminary study is that the questions of hydrogen production,: local detona-ble concentrations, combustion, and combined effects need to be considered in more detail as they apply to the BWR Grand Gulf. system in particular and the s BWR suppression pool concept in general.
-6 .
k l I f3 e (2p _. ,_ i i
REFERENCES
-1.
S. W. Hatch, P. Cybulskis and R. O. Wooton, " Reactor Safety Study O Methodology Applications Program: Grand Gulf #1 BWR Power Plant," NUREG/CR-1659/4, SAND 80-1897/4,(October 1981).
- 2. W. Hodges, " Comments on Draft of the Reactor Safety Study Methodology Applications Program Results for the Grand Gulf #1 BWR Power Plant," NRC Internal Memo, (March 24,1981).
- 3. R. D. Gasser, "An Assessment of Postulated Degraded Core Accidents in the
, Grind Gulf Reactor Plant," BNL-NUREG-DRAFT Report, (June 1982).
- 4. S. R. Greene, et al., "SBLOCA Outside Containment at Browns Ferry Unit One - Accident Segeence Analysis," Appendix B, NUREG/CR-2672, Volume I, (1982).
~
- 5. R. O. Wooton, H. I. Avci, " MARCH Code. Description and User's Manual ," ,
i NUREG/CR-1711, Battelle Nat16nal Laboratory, (October 1980). ; '] 5. J. W. Yang, " MARCH Analysis of Hydrogen Burning During Degraded Core I [ Accidents for the Clinton Power Station," BNL Internal Memo, (June 1982). l
- 7. " Assessment of BWR Mitigation on ATWS," General Electric Co., NEDE-24222, y
l- (December 1979). l [ 8. E. D. Fuller, et al., "BWR/6 Nuclear System From General Electric: A 1,
; Performance Description,' General Electric Co., NEDO-10569-A, (April l: 1972)..
l l' i i , ;
-. _t t:
4 APPENDIX A
; CASE DEFINITIONS 4
7-
>q ,
.;. Accident ECCS ECCS Contain H 2 Page
; Case # Sequence Inject. Recir.* CHRS Failure Burns #
GGTPWI TPW 1 0 0 0 1 A1 -
., . GGTPW2 TPW 1 1 0 0 1 'A24
- GGTPW3 TPW 1- 0 ~0 1 1 A47
', GGTW1 TW 1- 0 0 0 1 A70-4 GGTW2 TW 1 1 0 0 1 A93 GGTW3 TW 1 0 0 1 'l A118 j GGS2W1 SW 2 1 0 0 0 1 A142 GGS2W2 5W 2 1 1 0 0 1 A165 GGS2W3 SW 2 1 0 0 1 1 A185 ,
GGTQUV1 TQUV 0 0 0 0 1 A211 GGTQUV2 TQUV 0 0 0 1 1 A233 g ?h GGTQUV3 TQUV 0 0 0 1 0 A256
., - GGTPQE1 TPQE O O O O 1 A278 GGTPQE2 TPQE O 'O O 1 1 A302 r GGTPQE3 TPQE O O O 1 0 A324 l-(_ GGS2E1 SE 2 O O O O 1 A347 l, GGS2E2 SE 2 O O O 1 1 A370
( . GGTC1 TC 1 0 1* 0 1 A392 GGTC2 TC . 1 0 1* 0 1 A417 [ L i l' 0 - No 1 1 - Yes ]
- Failure in recirculation assumed due to pump cavitation.
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