Text

Bounding Analytical Assessment of NUREG-0630 Models on LOCA Kw/Ft Limits W/Use of Flecset
	ML20080L848
Person / Time
Site:	Arkansas Nuclear
Issue date:	09/30/1983
From:	; BABCOCK & WILCOX CO.
To:	;
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ML20080L841	List: 1CAN098310, Forwards B&W Owners Group Final Rept, Bounding Analytical Assessment of NUREG-0630 Models on LOCA Kw/Ft Limits W/Use of Flecset. Approval Requested; ML20080L848;
References
	RTR-NUREG-0630, RTR-NUREG-630 77-1140898-01, 77-1140898-1, TAC-53509, NUDOCS 8310030356
	Download: ML20080L848 (108)
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{{#Wiki_filter:- - - - - - - BOUNDING ANALYTICAL ASSESSMENT OF NUREG 0630 MODELS ON LOCA kW/ft LIMITS WITH USE OF FLECSET 1 l hhR DO ' OOO 3 p PDR l r 17 1140898-01 Babcock &Wilcox "' """ *P "Y September 1983 (

\\ i l l I .i 4 4 1 i f i BOUNDING ANALYTICAL ASSESSMENT OF NUREG 0630 MODELS ON LOCA kW/ft LIMITS WITH USE OF FLECSET-B&W Document No. 77-1140898-01 t BABC0CK & WILC0X Utility Power Generation Division { P.O. Box 1260 .Lynchburg, Virginia 24505 L

CONTENTS Page 1. INTRODUCTION........................... 1-1 2. SINMARY AND CONCL USION...................... 2-1 3. NURE G- 063 0 L OC A L IM IT AN ALY SI S.................. 3-1 3.1. Method of Analysi s..................... 3-1 3-1 3.2. Results of Analysis 4. JUSTIFICATION FOR USE OF FLECHT-SEASET HEAT TRANSFER CORRELATION FOR GENERATING REFLOOD HEAT TRANSFER COEFFICIENTS 4-1 4.1. Heat Transfer 4-1 4.2. Application of FLECSET2 at 2-and 4-ft Core Elevations -- Bottom Skewed Power Shapes................. 4-2 4.3. Application at 6-ft Core Elevation Symmetric (Cosine) P owe r Sha pe s........................ 4-4 4.4. Application at 8-and 10-ft Core Elevations -- Ou tl e t Sk ewed P owe r Sha pe s................. 4-4 5. SENSITIVITY OF PEAK CLAD TEMPERATURE TO REFLOOD HEAT TRANSFER COEFFICIENTS AT THE 2-Ft CORE ELEVATION 5-1 j 6. REF E R ENC E S............................ 6-1 APPENDIXES A-1 A. Excerpted From WCAP-9699 B. FLECSET -- A Computer Program to Calculate Heat Transfer B-1 Coefficients During Reflooding List of Tcbles Table 3-1. NUREG-0630 With FLECSET Offset LOCA Limit Impact at 2-f t Core Elevation, 8.55-f t2 DEPF, CD = 1.0 3-3 3-2. 177-FA Lowered-loop Plant LOCA Limits for BOL 3-4 4-1. Summa ry of LOC A Limi ts................... 4-5 4-2. Heat Transfer Coefficient Versus Time 4-6 4-8 4-3. Flooding Rates Versus Time - iii - t

List of Figures Figure Page 3-1. B&W Model and ORNL Correlation of Rupture Temperature as a Function of Engineering Hoop Stress and Ramp Rate....... 3-5 3-2. B&W THETA Model and Composite NUREG Correlation of Circumferential Burst Strain as a Function of Rupture Temperature 3-6 3-3. B&W Model and Composite NUREG Correlation of Reduction in Assembly Flow Area as a Function of Rupture Temperature.... 3-7 3-4. Hot Spot Clad Temperature Ys Time With NUREG-0630 and FLECSET -- 14.0 kW/ft at 2-f t Core Elevation 3-8 4-1. FLECSET Heat Transfer Coefficient Versus Tine at 2-ft Core Elevation,14.0 kW/ft 4-9 4-2. Heat Transfer Coefficient Versus Time at 2-ft Core Elevation,14.0 kW/ft 4-10 4-3. Heat Transfer Coefficient Versus Time at 4-ft Core Elevation,16.6 kW/ft 4-11 4-4. Heat Transfer Coefficient Versus Time at 6-ft Core Elevation,18.0 kW/ft 4-12 4-5. Heat Transfer Coefficient Versus Time at 8-ft Core Elevation,17.0 kW/f t 4-13 4-6. Heat Transfer Coefficient Versus Time at 10-ft Core Elevation,16.0 kW/f t 4-14 4-7. Heat Transfer Coefficient Versus Time at 8-ft Core Elevation, 17.0 kW/ft With Reduced Flooding Rate for First 30 Seconds 4-15 4-8. Reflood Heat Transfer Coefficients Versus Time at 2-ft Core Elevation for Peak Power Shapes of 2, 4, and 6-f t...... 4-16 4-9. Reflood Heat Transfer Coefficients Versus Time at 2-ft Core Elevation for Peak Power Shapes of 2, 4, and 6-f t...... 4-17 4-10. Heat Transfer Coefficient Versus Time at 2, 4, 6, 8, and 10-ft Core Elevations With FLECSET HTC 4-18 4-11. Heat Transfer Coefficient Correlation Versus Data, Skewed Power Run 15132........................ 4-19 4-12. Large Break Analyses Code Interfaces 4-20 4-13. LOCA Limi ts -- Power Shapes.................. 4-21 4-14. Quasi Steady-State Heat Transfer Coefficient Versus Distance From Quench Front for a Skewed Power FLECHT Run 15305..... 4-22 5-1. 2-ft Heat Transfer Coefficients Vs Time Generic LBLOCA Analysi s for 177-FA-LL Pla nts................. 5-2 5-2. Peak Cladding Temperature Vesrsus Time Generic LBLOCA Analysi s for 177-FA-LL Plants................. 5-3 5-3. Peak Cladding Temperature Versus Time Generic LBLOCA Analysis for 177-FA-LL Plants................. 5-4 5-4. Peak Cladding Temperature Versus Time Generic LBLOCA Analysi s for 177-FA-LL Pla nts................. 5-5 - iv -

1. INTRODUCTION l have been perfomed by B&W on behalf of the Supplemental ECCS calculations B&W Owners Group, based on a generic, bounding assessment of the impact of NUREG-0630 on loss-of-coolant accident (LOCA) kW/ft limits. These calcula-tions were performed for the 2 ft core elevation and the resulting reduction in kW/ft limit applied equally at the 4 and 6 foot core elevations. This analysis, which did not use compensating models to offset lost margin, re-suited in a 0.5 kW/f t reduction on the LOCA kW/ft limits due to the use of NUREG-0630 bounding models. In an effort to reduce or eliminate this 0.5 kW/ft penalty, the B&W Owners Group has established the need to consider the use of compensating models. The FLECHT-SEASET heat transfer correlation is used to generate reflood heat transfer coefficients. This correlation is modeled in the computer program named FLECSET. The work perfomed herein is an extension of the bounding analyses assess-ment previously perfomed.1 The use of the FLECHT-SEASET reflood heat transfer correlation as a compensating model results in a higher allowable kW/ft limit thus resulting in regained operating margin in the technical specification operating limits. 1-1 Y

2.

SUMMARY

AND CONCLUSION An ECCS bounding analysis was performed with a compensating model, FLECSET, to determine the offset of the NUREG-0630 penalty on B&W 177-fuel assembly (FA) lowered-loop plants operating LOCA limits. The break analyzed was an 8.55-ft2 double-ended cold leg rupture at the RC pump discharge with a dis-charge coefficient of CD = 1.0. The LOCA limit was evaluated for the 2-ft core elevation. Previous experience has demonstrated this elevation to be the most sensitive with respect to clad swelling and rupture phenomena. Implementation of NUREG-0630 with the FLECHT-SEASET reflood heat transfer correlation resulted in no kW/ft penalty on the LOCA limit at the 2-f t core elevation. An engineering assessment was performed for the 4 through 10-ft LOCA limits. For the 4-f t core elevation, there is no penalty due to the implementation of NUREG-0630 for the following reasons: (1) based on previ-ous analysis, the peak ruptured node cladding temperature was calculated to 7 be 1899F; therefore, sufficient temperature margin exists to meet the 10 CFR 50.46 criteria of 2200F, and (2) the FLECSET compensating model results in a higher allowable kW/ft limit, thus resulting in no impact to the LOCA limit at the 4-ft core elevation. For the 6-ft core elevation, the peak ruptured node cladding temperature 7 was calculated to be 2090F. Therefore utiliza-tion of FLECHT-SEASET at the 6-ft core elevation is not expected to pro-vide sufficient temperature margin to compensate for a 0.5 kW/f t penalty. For the 8-and 10-ft core elevations, the peak ruptured node cladding temp-7 was found to be 1664 and 1560F, respectively. There is considered erature to be sufficient temperature margin to satisfy the 2200F limit required by L 10 CFR 50.46. Therefore, no LOCA limit penalty is imposed at the 8-and 10-ft core elevations. The 4 through 10-f t LOCA limits, based on NUREG-0630 and the compensating model, FLECSET, are based on comparisons to the results i at the 2-ft core elevation and are engineering judgements. i 2-1 Y

The analysis was performed for the beginning-of-life (BOL) conditions at which the average fuel temperature is at its maximum value. At higher burn- ) ups, the lower fuel temperature will result in a greater LOCA kW/ft margin when compared to BOL. A summary of the final results at the 2-ft core elevation along with those given in references 1 (with NUREG-0630 plus TACO 2) and 7 (with TAC 02 fuel mode 13 only) are shown in Table 3-1. The 177-FA lowered-loop plant LOCA limits for BOL are listed separately in Table 3-2. Justification for use of the FLECSET code, utilizing the FLECHT-SEASET heat transfer correlation, for generating reflood heat transfer coefficients is also provided. This justification is based on -(1) comparisons of calculated heat transfer coefficients calculated by FLECSET with those calculated by the present LBLOCA Evaluation Model, (2) comparison with experimental data, and (3) sensitivity studies. Reflood heat transfer coefficients versus time were calculated for the 2, 4, 6, 8-and 10-ft. elevations using FLECSET and compared to those calcu-lated by the present LBLOCA Evaluation model BAW-10104, Rev. 3.5 The FLECSET reflood heat transfer coefficients at the 2-ft core elevation. are i 9 significartly higher than those calculated by FLECKA, during the early stage of the reflood phase. These higher reflood heat transfer coefficients allow the peak cladding temperature to be able to turn over much earlier in the transient. The significance of this is to allow a gain of 0.5 kW/ft to the LOCA limit over that predicted by the original FLECKA9 evaluation model. l The FLECHT-SEASET heat transfer correlation 2 has been developed based on the concept that the heat transfer coefficient is a function of the distance from the quench front and that the integral of power is used, thus the FLECSET correlation 2 is considered to be a more accurate code than FLECKA9 and would be applicable to predict reflood heat transfer coefficient to both skewed and cosine power shapes at any given core elevation. The use of FLECSET2 for calculating reflooding heat transfer coefficients at the 2-ft core elevation is therefore applicable. 2-2

2 at the 4, 6, 8, Reflood heat transfer coefficients predicted by FLECSET and 10-ft are comparable to those generated by the FLECKA9 (at the 4-and 6-ft core elevations) and by the REFLECHT10 (at the 8-and 10-f t core eleva-tions) models, and are shown to be in good agreement with those reported in WCAP-98912 and WCAP-969911 2-3 )

3. NUREG-0630 LOCA LIMIT ANALYSIS 3.1. Method of Analysis The analytical methods used in the present study are the same as those de-scribed in the B&W ECCS evaluation model topicals, BAW-10103A, Rev. 34 and 5 BAW-10104, Rev. 3, and the bounding analysis of the impact of NUREG-06301 on LOCA and operating kW/ft limits except for the modifications explained in the following paragraph. Figures 3-1 through 3-3 show the NUREG-0630 bound-ing parameters as described in detail in reference 1. A computer code called FLECSET,8, which was developed to predict the quench 2 time and heat transfer coefficient for cosine as well as skewed power shapes, was used in this analysis'. The present study consisted of running FLECSET at 14.0 kW/ft using input on flooding rates obtained from the recent bounding analysis. THETA 1-B6 l was used to generate the hot channel re-sponse at the 14.0 kW/f t LOCA limit. The peak cladding temperature was com-pared to the 10 CFR 50.46 limit of 2200*F to detennine acceptability. This analysis was performed only for the 2-ft core elevation and was consistent with the approach taken for the bounding analyses of NUREG-0630 models.1 3.2. Results of Analysis 7 The results of this analysis are summarized and compared to the base case and NUREG-06301 limits analyses Table 3-1. The maximum clad temperature for NUREG-0630 plus FLECSET case was calculated as 1847 and 1809'F for the rup-tured and unruptured nodes, respectively, as shown in Figure 3-4. These re-suits were calculated based on a 14.0 kW/ft limit at the 2-ft core eleva-tion. 3-1

As indicated in reference 1, there was an impact of 0.5 kW/ft for the 2, 4, and 6-ft core alevations due to the implementation of N UREG-0630. However, based on the results obtained on the present study, it is shown that, using NUREG-0630 with the FLECSET heat transfer correlation, no LOCA impact has been found at the 2-ft core elevation. This is because of the higher heat transfer coefficients generated by the FLECSET compensating model, which in turn resulted in a higher allowable kW/ft limit. A 0.5 kW/ft NUREG-0630 penalty was also previously assigned to the 4-- and 6~ ft core elevations. These elevations are also kW/ft limited by the rup-tured node temperatures. The peak cladding temperatures results at these respective elevations were reviewed with the improved FLECSET heat transfer ~ correlation. For the 4-ft core elevation, there should be no penalty due to the implementation of NUREG-0630 for the following reasons: (1) based on I 7 previous analysis, the peak ruptured node cladding temperature was calcu-lated to be 1899'F; there should be sufficient temperature margin to meet the 10 CFR 50.46 criteria of 2200*F and (2) the improved FLECSET compen-sating model is expected to result in a higher allowable kW/ft limit, thus it should allow the LOCA limit at the 4-ft core elevation to remain the 4 same. However, for the 6-ft core elevation, the peak ruptured node cladding temperature was calculated to be 2090*F and there nay not be enough tem-7 [ perature margin to meet the 2200*F requirements stated in 10 CFR 50.46. Also, FLECSET may not be able to provide sufficient temperature margin to compensate the 0.5 kW/ft penalty on the LOCA limit at the 6-ft core eleva-tion. For the 8-and 10-ft core elevations, the peak ruptured node cladding temperature 7 was found to be 1664*F and 1560*F, respectively, there should be sufficient temperature nargin to satisfy the 2200*F limit required by 10 CFR 50.46. Therefore, there should be no penalty on the LOCA limit at the 4 8-and 10-ft core elevations as given in BAW-10103A, Rev. 3. A summary of the latest 177-FA lowered loop plant LOCA analyses showing the 7 1 impacts of TACO 2, NUREG-0630, and the NUREG-0630 with FLECSET are shown in Table 3-2. l l l 3-2 L

Table 3-1. NUREG-0630 With FLECSET Offset LOCA Limit 2 Impact at 2-f t Core Elevation, 8.55-f t DEPD, CD = 1.0 NUREG-0630 Base case 7 NUREG-06301 FLECSET CRAFT run AD4ICLD AD4IDWU AD4IDWU REFL003 run AD4IBKD AD41VUS AD41VUS THETA 1-B run AD4ICCA AD4IEYW AEKIBUH CRAFT,kW/ft 14.5 14.0 14.0 THETA 1-B, LOCA limit 14.0 13.5 14.0 Peak temperature, 'F, unrup-1843/43.5 1692/42.5 1809/37.0 tured node / time, s Peak temperature, F, rup-1934/43.5 1736/42.0 1847/37.3 tured node / time, s Rupture time, s 21.6 22.6 17.9 End of blowdown, s 25.2 24.8 24.8 End of adiabatic heatup, s 36.0 35.5 35.5 Maximum local oxidation, % 2.14 1.52 1.67 CRAFT 2 blockage, % 58.8 67.65 67.65 i r t 3-3 J

Table 3-2. 177-FA Lowered-Loop Plant LOCA Limits for BOL Core elevation, ft 2 4 6 8 10 BAW-10103 LOCA limits,4 kW/ft 15.5 16.6 18.0 17.0 16.0 TAC 02 impact,7 kW/ft -1.5 0 0 0 0 NUREG-0630(a) impact, kW/ft -0.5 -0.5 -0.5 0 0 l NUREG-0630 LOCA Limits 13.5 16.1 17.5 17.0 16.0 FLECSET-offset,kW/ft +0.5 +0.5 0 0 0 i NUREG-0630 + FLECSET(b) LOCA limits, kW/ft 14.0 16.6 17.5 17.0 16.0 (a)LOCA limits for 4-and 6-ft core elevations can be restored to 16.6 and 18.0 kW/ft, respectively, after a burnup of 1000 mwd /mtV. The 2-ft LOCA limit can be increased to 15 kW/ft after a burnup of 1000 mwd /mtU and restored to 15.5 kW/ft after a burnup of 2600 mwd /mtU. 4 (b)The 2-and 6-ft LOCA limit can be restored to 15.5 and 18.0 kW/ft, respectively, after a burnup of 1000 mwd /mtU. i 3-4

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1 I 4. JUSTIFICATION FOR USE OF FLECHT-SEASET HEAT TRANSFER CORRELATION FOR ENERATING REFLOOD HEAT TRANSFER COEFFICIENTS 4.1. Heat Transfer j l The analytical methods used to evaluate reflocd heat transfer coefficients I are the same as those described in section 4.3.6.5 of B&W ECCS evaluation model topical report BAW-10104, Rev. 35 except for the following modifica-tions. In place of the FLECKA9 and REFLECHT10 evaluation models, the FLECSET model f is used. FLECSET is the name of the computer code which uses the FLECHT-SEASET correlation for the calculation of reflooding heat transfer coefficients. FLECKA5 calculates heat transfer coefficients for the 2, 4, and 6-ft core elevations based on flooding rates calculated by the REFLOD3 code.12 REFLECHT10 is used at the 8-and 10-ft core elevations to generate equivalent flooding rates that are then input to FLECKA9 to calculate re-flood heat transfer coefficients. Unlike the correlation contained in FLECKA9 and REFLECHT10, the FLECHT-SEASET heat transfer correlation 2 was de-veloped based on both cosine and skewed power shapes, as shown typically in Figure 4-13. The FLECHT-SEASET correlation 2 is valid for the following ranges of parameters: flooding rate, constant or variable, from 0.4 to 10.0 in./s; system pressure,15 to 60 psia; inlet subcooling,16 to 140*F; ini-tial clad temperature, 300 to 2200*F and equivalent peak power, 0.3 to 2.0 kW/ft. The FLECHT-SEASET correlation 2 conserves the integrated power at dif-ferent core elevations. Figure 5-12 shows how the FLECSET code 2 interfaces with the other ECCS large break LOCA codes. To justify the use of FLECHT-SEASET correlation 2 as a compensating model, an evaluation has been performed at the 2, 4, 6, 8, and 10-ft core eleva-tions using the core flooding rates shown in Table 4-3. This analysis has ( been performed with equivalent key parameters (flooding rates, system pres-sure, peak rod power, inlet subcooling, initial clad temperature and power 4-1

shapes) and has been consistent with the approach taken for the TAC 02 LOCA limits analysis.7 The results of this analysis are summarized and compared to those given in reference 7 as shown in Figures 4-1 ^.hrough 4-10. 2 at 2-and 4.2. Application of FLECSET 4-ft Core Elevations -- Bottom Skewed Power Shapes As indicated in WCAP-9891,2 the FLECHT-SEASET reflood heat transfer correla-tion has been based on the experimental data calculated at the core mid-plane and core exit regions. However, the FLECHT-SEASET correlation, as discussed in reference 13, has also been designed on the concept of consider-ing the heat transfer coefficient to be a function of the distance from the quench front for all levels below the PCT elevation, and to be a function of the distance from the PCT elevation for all levels above it. The heat trans-fer coefficient is primarily a function of the distance from the quench front because the heat transfer required on an unwetted cladding surface 8 starts its development from the quench front. As suggested in WCAP-9183, the FLECHT-SEASET correlation 2 could be used to predict the quench front movement of both skewed and cosine power shapes at any elevation by using the ratio of the integral of power. Quench time has been shown to be propor-tional to the heat input below the quench front.13 This heat can be reason-ably approximated by the integral of power below the quench front. The re-suits reported in reference 8 were found to be in good agreement. There-fore, the FLECHT-SEASET reflood heat transfer correlation 2 is considered applicable for predicting heat transfer coefficients as a function of dis-tance from the quench front to both skewed and cosine power shapes and at any given core level above or below the peak clad temperature elevation. The reflood heat transfer coefficients versus time calculated by the FLECSET code at the 2-ft core elevation, as shown in Figure 4-2, are significantly 9 higher than those predicted by FLECKA, especially for the first 10 seconds following the end of adiabatic heatup. These higher reflood heat transfer coefficients are justified based on the following reasons: ( 4-2

1. They are in good agreement with those provided by the Westinghouse PWR FLECHT-SEASET test da ta reported in WCAP-969911, for compatible key parameters as shown in Table 4-2. The heat transfer coefficients at the 1-and 2-f t core elevations are found to be consistently higher than those at the 4-and 6-ft core elevations, reported in runs 31203, 31302, 34420, and 34524 of WCAP-9699, which have been excerpted and included as Appendix A. 2. As indicated in reference 13 (run 15305) reflood heat transfer coeffi-cients are found to be increasingly higher as distance moves closer toward the quench front, especially within the range of 3-ft above the quench front (i.e.,1-and 2-ft elevations) as shown in Figure 4-14. This rapid rise in the reflood heat transfer coefficient is due to the high proportion of injected water being entrained during the early stage of the reflood phase and carried out of the rod bundle thus improving heat transfer To determine the effect on the reflood heat transfer coefficients due to the change in ratio of the integral of power, two separate runs have been per-formed using the 4-and 6-ft 1.7 axial power shapes as shown in Figure 4-13 with the same flooding rates as the 2-ft core elevation. The results show that there is very little difference in the 2-f t reflood heat transfer coef-ficients using the 2, 4, and 6-ft power shapes for the first 10 seconds following the end of adiabatic heatup. However, after 15 seconds following the end of adiabatic heatup, the reflood heat transfer coefficients at the 4-and 6-ft core elevations start to become higher than those at the 2-ft core elevation. This is shown in Figures 4-0 and 4-9. Thus, the effects of power on the reflood heat transfer coefficients during the early stage fol-lowing the end of adiabatic heatup are considered to be negligible. Reflood heat transfer coefficients versus time at the 4-f t core elevation 2 predicted by FLECSET, as shown in Figure 4-3, are comparable to those calcu-lated by FLECKA9 given in reference 7. Similar results were also found in all four cases reported in WCAP-969911 shown in Table 4-2 and in Appendix A. Thus, it is concluded, based on the similarity of results, that the FLECHT-SEASET reflood heat transfer correlation 2 contained in the FLECSET code is applicable for predicting heat transfer coefficients at the 4-ft core eleva-tion. 4-3 i

4.3. Application at 6-ft Core Elevation Syninetric (Cosine) Power Shapes The reflood heat transfer coefficients versus time at the 6-f t core eleva-tion calculated by the FLECSET2 code are reasonably comparable to those 9 evaluation model, as shown in Figure 4-4. Al so, predicted by the FLECKA results reported in WCAP-969911, (shown in Table 4-2 and Appendix A) and in the benchrirk tests (shown in Figures 6-6 and 6-7 of Appendix B) were found to be in got i agreement. Therefore, the FLECSET reflood heat transfer cor-relation 2 is also applicable to predict the reflood heat transfer cceffi-cient at the 6-ft core elevation. 4.4. Application at 8-and 10-ft Core Eleva-tions -- Outlet Skewed Power Shapes The reflood heat transfer coefficients versus time calculated using FLECSET at the 8-and 10-ft core elevations are reasonably comparable to those pre-dicted by REFLECHT10 shown in Figures 4-5 and 4-6, respectively. The rapid rise in reflood heat transfer coefficient at both 8-and 10-ft core eleva-tions during the early stage of the reflood phase wa s also found in 2 WCAP-9891, as shown in Figure 4-11. To detennine any possible effect cn FLECSET heat transfer coefficient predictions due to initial flooding rates, a study has been perfomed at the 8-f t core elevation, by reducing the ini-tial flooding rates for the first 30 seconds following the end of adiabatic hea tup. The calculated FLECSET results, which are shown in Figure 4-7, indi-cate a substantial drop in heat transfer coefficient during the early period following the end of adiabatic heatup. A similar trend was also found in the test results reported in reference 2. Thus, the reflood heat transfer correlation in FLECSET is suitable for predicting heat transfer coefficients at the 8-and 10-ft core elevations. 1 ( 4-4 L_

u ~ Table 4-1. Summary of LOCA Limits Distance from bottom of core, ft 2 4 6 8 10 CRAFT / THETA LHR, kW/f t 14.5/14.0 16.6/16.6 18.0/18.0 17.0/17.0 16.0/16.0 l CFT actuation time, s 17.6 17.4 17.4 17.4 17.4 Rupture time / blockage, % 21.6/58.8 23.6/61.12 23.2/60.10 25.3/62.34 27.3/64.47 End of blowdown, s 25.2 25.0 24.8 24.6 24.8 End of bypass, s 25.2 25.0 24.8 24.6 24.8 Mass remaining in vessel at 16 04.0 1902.0 1782.0 1616.0 1878.0 end of blowdown, Ibn { End of adiabatic heatup, s 36.0 35.7 35.8 35.3 35.6 Peak unruptured node cladding 1843/43.5 1874/42.5 2030/43.0 1848/143.7 1773/210.9 temperature / time, F/s 1 Peak ruptured node cladding 1934/43.4 1899/42.6 2090/44 1664/39.5 1560/39.5 temperature / time, F/s l Local metal-water reaction, % 2.12 1.90 3.92 2.12 1.78 Initial pin pressure, psia 1555 1555 1555 1555 1555-

Table 4-2. Heat Transfer Coefficient Versus Time Time h(af h(af h(af h(a (Btu /h-ft}-T) after h 2 E0AH, s (Btu /h-ft -T) (Btu /h-ft -T) (Btu /h-ft -T) (Btu /h-ft -T) 2-ft Core Elevation Reference 4 Reference 7 Reference 7 Reference 7 Reference 7 Peak power run No. AEKIKQD run No. 31203 run No. 31302 run No. 34420 run No. 34524 Tsub 0.75 kW/ft 0.70 kW/ft 0.69 kW/ft 0.74 kW/ft 1.0 kW/ft T nit 145T 126T 126T 124T 1257 i pressure 1900T 1601T 1597T 2045T 1612Y inlet 40 psia 40 psia 40 psia 39 psia 40 psia velocity variable FR 1.51 in./s 3.01 in./s 1.53 in./s 1.57 in./s 0.0 3.6459 4.0 4.0 3.0 3.0 (FR=2.758 in./s) [ 10.43 21.795 22.0 40.0 24.0 28.0 (FR=2.332 in./s) 19.68 23.8769 35.0 60.0 40.0 41.0 (FR=1.743in./s) 4-ft Core Elevation Reference 4 Reference 7 Reference 7 Reference 7 Reference 7 Peak power run No. AEKIDD0 run No. 31203 run No. 31302 run No. 34420 run No. 34524 T ub 0.89 kW/ft 0.70 kW/ft 0.69 kW/ft 0.74 kW/ft 1.0 kW/ft sTinit 145T 126T 126T 124T 1257 pressure 1800T 1601T 1597T 2045T 1612 T inlet 38 psia 40 psia 40 psia 39 psia 40 psia velocity variable FR 1.51 in./s 3.01 in./s __ 1.53 in./s 1.57 in./s 0.0 4.2576 2.0

2. 0 3.0

2. 0 (FR=2.7872 in./s) 10.47 12.5923

7. 0 18.0 8.0

7. 5 (FR=2.385in./s)

~

Table 4-2. (C ont 'd) Time h(af h(af (Btu /h-ft}-T) (Btu /h-ft}-T) h(a h(a after h 2 E0AH, s (Stu/h-ft -T ) (Btu /h-ft -T) (Btu /h-ft - T ) 4-ft Core Elevation (Cont') 22.08 13.6682 12.0 22.0 16.0 14.0 (FR=1.799 in./s) l 41.81 13.9893 213.0 40.0 20.0 20.0 (FR=1.479 in./s) 6-ft Core Elevation Reference 4 Reference 7 Reference 7 Reference 7 Reference 7 j Peak power run No. AD4IE0A run No. 31203 run No. 31302 run No. 34420 run No. 34524 7 Tsub 0.96 kW/ft 0.70 kW/ft 0.69 kW/ft 0.74 kW/ft 1.0 kW/ft T nit 145T 126Y 126T 124T 125T i pressure 1900T 1601T 1597T 2045T 1612Y inlet 43 psia 40 psia 40 psia 39 psia 40 psia I velocity variable FR 1.51 in./s 3.01 in./s 1.53 in./s 1.57 in./s O.0 4.3812 2.0 3.0 2.3

2. 0 (FR=2.809 in./s) 10.91 11.8943 8.0 16.0

6. 0 5.0 (FR=2.41in./s) 21.36 12.2576 10.5 20.0 11.0 9.0 (FR=1.838 in./s) 40.46 11.2335 10.6 24.0 13,0 12.0 (a) Extrapolated values from test data given in reference 7.

FR = flooding rate at time following end of adiabatic heatup (E0AH).

f. Table 4-3. Flooding Rate Versus Time Core Time after Flooding elevation, end of adiabatic rate ft heatup, s in./s 2 0.0 to 9.29 2.758 9.3 to 14.29 2.332 14.3 to 30.29 s 1.743 30.3 to 57.29 1.427 57.3 to end of run 1.35 4 0.0 to 9.072 2.7872 9.037 to 14.072 2.385 14.073 to 29.272 1.799 29.273 to 53.272 1.479 53.273 to end of run 1.379 6 0.0 to 9.218 2.809 9.219 to 14.219 2.410 14.22 to 29.22 1.838 29.23 to 55.23 1.513 55.24 to end of run 1.407 8 0.0 to 5.063 2.793 5.064 to 30.263 2.2141 30.264 to 65.263 1.539 65.264 to 89.263 1.4361 89.264 to 139.263 1.3979 115.264 to 139.263 1.3604 139.264 to 165.263 1.3121 165.264 to 191.263 1.2447 191.264 to 215.263 1.1746 215.264 to 241.263 1.100 l 241.264 to 267.263 1.0228 l 267.264 to end of run 0.9531 10 0.0 to 5.038 2.8993 5.039 to 20.238 2.8029 20.239 to 65.238 1.5987 65.239 to 89.238 1.4727 l 89.239 to 115.238 1.4112 l 115.239 to 141.238 1.3386 141.239 to 165.238 1.2547 l 165.239 to 191.238 1.1618 191.239 to 217.238 1.0626 217.239 to 241.238 0.9728 241.239 to 267.238 0.8832 267.239 to 291.528 0.802 l 291.529 to end of run 0.8 02 t j i l 4-8 L.

t Figure 4-1. FLECSET Heat Transfer Coefficient Versus Time at 2-ft Core Elevation, 14.0 kW/ft 100 RUN # = AEKlKQD, AEKilVD, _p PRESSURE = 40.0 PSI A m' PEAK POWER =.75 KW/FT U FLOODING RATE = VAR. FR-TABLE 4-3 80 INLET SUBC00 LING = 145'F i INITI AL TEMP. = 1900'F g ELEVATION = 2.0 FT. J 60 ^ g .2 I j 40 MR = 2. UN I F. P. A EKi l %D

MR = 1. RADI AL P. AEKlKQD u3 E.

20 E O - I I I I I I I O 10 20 30 40 50 60 70 Time Following End of Adiabatic Heatup, s 4-9

Figure 4-2. Heat Transfer Coefficient Versus Time at 2-f t Core Elevation,14.0 kW/f t 100 RUN # = AEKICDX, AEKlKQD c PRESSURE = 40.0 PSI A PEAK POWER =.75 KW/FT FLOODING RATE = VAR. FR-TABLE 4-1 80 i INLET SUBC00 LING = 145*F INITI AL CLAD TEMP. = i900*F ELEVATION = 2.0 FT. = S FLECKA AEKICDX 60 FLECSET AEKlKQD .I MR = 1. RADI AL P. .2 40 j b t g 20 y 7 ,e = 0 I I I I I I I l 0 10 20 30 40 50 60 70 Time Fc11owing End of Adiabatic Heatup, s } 4-10

Figure 4-3. Heat Transfer Coefficient Versus Time at 4-ft Core Elevation,16.6 kW/ft 50 RUM # = AD41 FMR, AEK1000 PRESSURE = 38.0 PSI A PEAK POWER =.89 KW/FT N, FLOODING RATE = VAR. FR-TABLE 4-3 i INLET SUBC00 LING = 145'F d INITI AL CLAD TEMP. = 1800'F ELEVATION = 4.0 FT. = O 30 C .{ FLECKA AD41FMR E --- FLECSET AEKI DD0 3 20 MR = i. RADIAL P. ~ ~ ~ g c h 10 / "o / 0 I I I I I I I O 10 20 30 40 50 60 70 80 Time Following End of Adiabatic Heatup, s f 1 i ( l 5 4-11

Figure 4-4. Heat Transfer Coefficient Versus Time at 6-ft Core Elevation,18.0 kW/ft 20.0 FLECKA AD41CMH -{ FLECSET A041 EDA 't MR = 1. RADIAL P. i 16.0 u

'i

$i2.0 /~~~~ ~\\ c I -{ ,/ RUN # = AD41 CMH, AD4t EDA PRESSURE = 43.0. PSI A p / PEAK POWER =.96 KW/FT S 8.0 ,i ) FLOODING RATE = VAR. FR-TABLE 4-3 b INLET SUBC00 LING = 145'F INITI AL CLAD TEMP. = 1900*F f ELEVATI ON = 6.0 FT. - 4.0 r E O I I I I I I I O 10 20 30 40 50 60 70 80 Time Following End of Adiabatic Heatup, s 4-12 s

-t r, Figure 4-5. Heat Transfer Coefficient Versus Time at 8-ft Core Elevation,17.0 kW/ft 20.0 p FLECKA(BAW-10103A,REV3) / FLECSET AD41EBZ { 16.0 /,. MR = 1. RADIAL P. g Q -..---------. -----,,a#' #'s**, / \\ 4 / \\ / y 12.0 g 1 i RUN # = AD41 EBZ i PRESSURE = 43.0 PSIA 8 PEAK POWER =.9 KW/FT 8 FLOODING RATE = VAR. FR-TABLE 4-3 ~ ch g g INLET SUBC00 LING = 145*F t f INI TI AL ' CLAD TEMP. = 1600*F 5 ELEVATION = 8.0 FT. A 4.0 L e I I I I l I I O O 20 40 60 80 iOO 1 20 140 160 Time Following End of Adiabatic Heatup, s l l L

1 ) Figure 4-6. Heat Transfer Coefficient Versus Time at 3 10-ft Core Elevation, 16.0 kW/ft i 20.0 c FLECKA (BAW-10103A, REV. 3) Od gg% FLECSET AD4tHUE 9 16.0 g NR = 1. RADIAL P u i s i ,/ s / \\ j 12.0 ~~ c I I .S l RUN # = AD41 HUE O e PRESSURE = 43.0 PSIA j 8.0 -s l PEAK POWER =.85 KW/FT L I FLOODING RATE = VAR. FR-TABLE 4-3 u 8 g INLET SUBC00 LING = 145'F j g" INITI AL CLAD. TEMP. = 1600*F { 4.0 h ELEVATION = 10.0 FT. - .i j 0 I I I I I I I j 0 20 40 60 80 100 120 140 160 Time Following End of Adiabatic Heatup, s j l t I 'm

r ~ Figure 4-7. Heat Transfer Coefficient Versus Time at 8-ft Core Elevation, 17.0 kW/ft With Reduced Flooding Rate for First 30 Seconds 20.0 FLECSET A041E8Z g FLECSET AEKIFME B w--- 16.0 REDUCED FR FOR F1RST 30 SEC. AFTER i ALL MR = 1. RADIAL P. d =g ~~~~----- ~~ ~ 12.0 RUN # = AD41EBZ, AEKl FME f o i PRESSURE = 43.0 PSI A 5 / PEAK POWER =.9 KW/FT a FLOODING RATE = VAR. FR-TABLE 4-3 8.0 p h j 1 INLET SUBC00 LING = 145'F I INITI AL CLAD TEMP. = 1600*F E /, ELEVATION = 8.0 FT. 2 4.0 / r e I I I I I I I 0 O 20 40 60 80 100 (20 140 160 Time following End of Adiabatic Heatup, s

) Figure 4-8. Reflood Heat Transfer Coefficients Versus Time at 2-ft Core Elevation for Peak Power Shapes of 2, 4, and 6-ft (all peak powers at 14.0 kW/ft) IN RUN # = AEKlKQD, AEKIMTP, AEKIMVQ PRESSURE = 40.0 PSI A o) PEAK POWER = VAR. KW/FT "O 80 FLOODING RATE = VAR. FR-TABLE 4-3 f' INLET SUBC00 LING = 145'F s' d iNITl AL CLAD TEMP. = 1900*F ,/,e# ELEVATION = 2, 4, 6 FT. 60 / f e s p* 4; 40 Y /l# .,-/. .E AEKl KQD, 2 FT. 4 20

AEKlMTP, 4 FT.

j --- AEKINVQ, 6 FT. = ALL MR = l. RADI AL P.FLECSET 0 I I I I l 0 10 20 - 30 40 50 60 70 I Time Following End of Adiabatic Heatup, s I i 4-16 1

Figure 4-9. Reflood Heat Transfer Coefficient Versus Time at 2-ft Core Elevation for Peak Power Shapes of 2, 4, and 6-ft (all peak powers at 14.0 kW/ft) 22.0 /, p' /./.s= ~ E 20.0 m' / / k 18.0 j RUN # = AEKlKQD, AEKIMPT, AEKINVQ 3 16.0 / PRESSURE = 40.0 PSI A [ PEAK POWER = VAR. KW/FT E FLOODING RATE = VAR. FR-TABLE 4-3 14.0 INLET SUBC00 LING = 145*F INITI AL CLAD TEMP. = 1900*F .2 12.0 0 ELEVATION = 2, 4, 6 FY. e O 10.0 o o t 8.0 5 A 6.0 e f 3 AEKlKQD, 2 FT. f = 4.0 f

AEK IM fP, 4 FT.

f

2. 0

AEKINVQ, 6 FT.

ALL MR = 1, RADI AL P. FLECSET HTC. O I O 2.0 4.0 6.0 8.0 10.0 12.0 Time Following End of Adiabatic Heatup, s r [ 4-17

Figure 4-10. Heat Transfer Coefficient Versus Time at 2, 4, 6, 8, and 10-ft Core Elevations With FLECSET HTC 52.0 8 FT. AD4fE8Z [RUN * = AEKlKQD, AEKIDDO, / AD418DA, AD41EBZ, f

10 FT. AD41 MUE AD41 HUE I

48.0 = = 2 FT. AEKlKQD, PRESSURE = VAR. PSIA PEAK POWER = VAR. KW/FT 44.0 - --4 PT. AEKIDD0/ FLOODING RATE = VAR. FR-f TABLE 4-3 ...... 6 FT. AD41ED INLET SUSC00 LING = 145'F 40.0 - INITIAL CLAD TEMP, = VAR., s og e' 8 N, ELEVATION = 2,4,6,8,10FT w 36.0 - ALL MR = 1. RADIAL P. 5, FLECSET HTC. / = E 32.0 - .8 / / ,3 28.0 e / / 3 24.0 u E 20.0 - [g 16.0 / i .s I e l

- - %............=*.- -
~ ~ ~ ~

i 2.0 e j i. 8.0 i 4.0 0 O 20 40 60 80 100 120 140 160 180 Time Follor:ing End of Adianatic Heatup, s 4-18

Figure 4-11. Heat Transfer Coefficient Correlation Versus Data, Skewed Power Run 15132 no s1.e4 PRESSURE = o.27 MPs (a peiel PEAK POWER = 2.3 kw/m (o.7 km/tt) l C FLOODING RATE = 152 suun/ses (6 mJessl 5 ses l k 3oo 2 3 suun/ses to.o indses) "g ONWARD - ll 5. 4 { g INLET SueCOOLING = 77'c (13e*F) l J

29.

INITIAL CLAD TEMPERATURE = odo*C (1966*F) E ~ 3 G ) E nOc so W E 2eo ROO 4G d E 38 f 3 nOo 7e u s 1to -..- CORRELATION i E ELEVATION 3.oS m (12e in.) E { l m I g wo [ l a~ to E j y gy I I I I I I I o no zoo soo noe ooo m ooo TiteE (ses) ( ( [ 4-19

Figure 4-12. Large Break Analyses Code Interfaces INITIAL RC SYSTEM & CORE PARAMETERS . INITIAL CORE PARAMETERS U I CRAFT MASS & ENERGY RELEASE CORE RESPONSE DURING BLOWOOWN y I II. CONTEMPT CONTAINMENT PRESSUf!E

RESPONSE

STORED ENERGY y ' f BACK PRESSURE VESSEL T INVENTORY g g III i

RECHT RER00 3 h(t)

~ FLOODING REFLOOD HEAT TRANSFER 1 f 1 f 1 I CDEFFICIENTS l \\ V THETA

FLECHT correlation to be re-HOT CHANNEL RESPONSE placed by the FLECHT-SEASET correlation (FLECSET Code)

I f j leT PIN THERMAL RESPONSE SURFACE HEAT TRANSFER COEFFICIENT HOT CHANNEL FLUID TEMPERATURE ETAL-WATER REACTION l b 4-20

21 = 11 01 a 01 9 i i 8 8 sep e a r h 7 o S e C re n w i o P n 6 i 6 o i t s t av im e i L 5 l E A CO L 3 4 . 4 1 4 eru g . 3 i F 2 . 2 . 1 0 8 6 4 8 6 4 2 0 a 1 1 1 1 1 0 0 0 m g-

u. o 5. t a34 i

m ?=

Figure 4-14. Quasi Steady-State Heat Transfer Coefficient Versus Distance From Quench Front for a Skewed Power Fl.ECHT Run 15305 1 REFLOOD IIEAT TRANSFER CORRELATION RUN NUMBER 15 305 - - - 75 s PRES $U RE 276 kPa (40 psia) -~~ 8 283.9 INITIAL CLA00 LNG E (50) 8 TEMPERATURE 871*C (1600*F)

400 s

'f CORRELATION PEAK POWER 2.30 kW/m (0.7 kW/ft) j SUBC00 LING ?!*C (140*F) S 227.1 INJECTION RATE 2.03 cm/s (0.8 mJs) l .y 140) g f CORRELATION g \\ PEAK POWER LOCATION g,,,, h 400 200 100 75 s s s s s 5 113.6 %p h f y y (20) g Y D-- \\ w._ 400 s - s 0 0 0.61 1.22 1.83 2 44 3.05 (2) (4) (6) (8) (10) j O! STANCE FROM QUENCH FRONT, Z -Ze im (f tll l I l l l J ) { i 4-22 -i

5. SENSITIVITY OF PEAK CLAD TEMPERATURE TO REFLOOD HEAT TRANSFER COEFFICIENTS AT THE 2-Ft CORE ELEVATION A comparison of reflood heat transfer coefficients at the 2-ft core eleva-tion has been performed using FLECKA and FLECSET at the same flooding rate and equivalent peak power of 14.5 kW/f t. Results indicate that the heat transfer coefficients calculated by FLECSET are significantly higher than those predicted by FLECKA for the first 37 seconds following the end of adiabatic heatup, as shown in Figure 5-1. The importance of the higher heat transfer coefficient predicted by FLECSET is shown in Figure 5-2', where the 2 is substantially lower and neak cladding temperature predicted by FLECSET turns around within the first 5 seconds when compared to that calculated with FLECKA heat transfer coefficients. The most critical heat transfer coefficients, as far as the PCT at the 2-ft core elevation is concerned, are those predicted within the first 10 seconds following the end of adiabat-ic heatup. Thus, the 14.5 kW/f t THETA ' case, using the heat transfer coeffi-2 cients generated by FLECSET heat transfer correlation, meets the PCT re-quirements of 2200*F as stated in 10 CFR 50.46. The PCT response of both ruptured and unruptured nodes evaluated at 14.5 kW/f t at the 2-ft core eleva-tion is shown in Figures 5-3 and 5-4, respectively. s ( 5-1 (

Figure 5-1. 2-ft Heat Transfer Coefficients Vs Time Generic LBLOCA Analysis for 177-FA-LL Plants 2 KEY g I4 5 KWlFT FLECSET ~ h %.0

14.5 KW/FT FLECKA 3

a*** f 30.0 ~ ~~ a 20.0 ~ ~ ~ ~ ~ ~ ~ C l E f p 10.0 - / +* / 5 / = 0.0 1 1 1 1 0.0 10.0 20.0 30.0 40.0 isne following End of Adibatsc Heatup, g a o

1 Figure 5-2. Peak Cladding Temperature Versus Time Generic LBLOCA Analysis for 177-FA-LL Plants C KEY 2200 g 14.5 KW/FT THETA (FLECKA H.T. C. 'S) I u

14.5 KW/FT THETA ( FLECSET H. T. C. 'S) 2 2l00

+ 14.0 KW/FT TH ETA ( FLECK A H. T. C. ' S) i

~,s r E s' \\ g 2000 u \\ mb b \\ \\ j /g 7 -%- a. 1900 e~~ s N \\ 1800 / g /*/ N % ) i i 1700 I I I I i i I 0.0 1.0

2. 0 3.0 4.0 5.0 6.0 7.0 8.0 9.0 10.0 l1.0 Time Following End of Adiabatic Heatup, s l

1

l Figure 5-3. Peak Cladding Temperature Versus Time Generic LBLOCA Analysis for 177-FA-LL Plants (ruptured node) ) 45.000 40.000 35.000 _u 7 w u. 30.000 2 3 2 25.000 E ~6 2069*F u j 20.000 i* m 15.000 l l l 10.000 I I I I 5.000 O.000 2.000 4.000 6.000 8.000 10.000 12.000 I Time (sec) (xiO ) 14.5 KW/FT AT 2.0 FT 5-4

Figure 5-4. Peak Cladding Temperature Versus Time Generic LBLOCA Analysis for 177-FA-LL Plants (unruptured node) ' I' 19.188 -

17. 375

^mb 3 o' 15.563 3-h 2 f { 13.750 E 'E l1.858 G E 10.125 8.313 6.500 I I I I I 0.000 2.000 4.000 6.000 8.000 10.000 12.000 I Time (sec) (x10 ) 14.5 KW/FT AT 2.0 FT ( 5-5 {.

6. REFERENC ES 1. "Boundi ng Analytical Assessment of NUREG-0630 on LOCA and Operating kW/ft Limits," B&W Docunent Nos. 77-1140894, 77-1140895, 77-1140896, 77-1140897, 77-1140899, 77-1141256, and 77-1142161. 2. N. Lee, S. Wong, H. C. Yeh, and L. E. Hochreiter, "PWR FLECHT SEASET Unblocked Bundle, Forced and Gravity Reflood Task Data Evaluation and Analysis Report, NUREG/CR-2256 (EPRI NI-2013 or WCAP-9891), November 1981. 3. TAC 02 - Fuel Pin Perfomance Analysis, BAW-10141P, Babcock & Wilcox, Lynchburg, Virginia, August 1979. 4. B. M. Dunn, et al., ECCS Analysis of B&W's 177-FA Lowered-Loop NSS, BAW-10103A, Rev. 3, Babcock & Wilcox,-Lynchburg, Virginia, July 1977. 5. B. M. Dunn, et al., B&W's ECCS Evaluation Model, BAW-10104, Rev. 3, Babcock & Wilcox, Lynchburg, Virginia, August 1977. 6. R. H. Stoudt, et al., THETA 1-B - Computer Code for Nuclear Reactor Thermal Analysis, NPGD-TM-405, Rev. L, Babcock & Wilcox, Lynchburg, Virginia. March 1982. 7 M.A. Haghi, et al., TAC 02 Loss-of-Coolant Accident Limit Analyses for 177-F A Lowe red-loop Plants, BAW-1775, Babcock & Wil cox, Lynchburg, Vi rginia, February 1933. 8. G. P. Lilly, et al., PWR FLECHT Skewed Profile Low Flooding Rage Test Series Evaluation Report, WCAP-9183, November 1977. 9. K. C. Heck, et al., "FLECKA, Procedure to Calculate Reflood Heat Trans-fer Coefficients," NPGD-TM-357, Babcock & Wilcox, March 1976 l 10. B. M. Dunn, et al., "REFLECHT Correlation," BAW-10091P, Appendix B, Babcock & Wilcox, August 1974. ( 6-1 )

I 11. L. E. Hochreiter, -et al., "PWR FLECHT SEASET Unblocked Bundle, Forced 3 and Gravity Reflood Task Data Report," Vol. 2, NUREG/CR-1532 L (EPRI-NP-1459 or WCAP-9699), June' 1980. 12. B. E. Bingh&m and K. C. Shieh, REFLOOD - Description of Model for Multinode Core Reflood Analysis," BAW-10093, Babcock & Wilcox, March 1974 13. H. C. Yeh, et al., "Refl ood Heat Transfer Correl ation," Nuclear Technoloqy 46, (1979) p. 473. 1 I I t 6-2

APPENDIX A Excerpted From WCAP-9699 l A-1

This section contains tables and plots used for data cmparisons in this re-port and were originally published in the following report: FLECHT SEASET Program NRC/EPRI/ Westinghouse Report No. 7 NUR EG/CR-1532 EPRI NP-1459 WCAP-9699 PWR FLECHT SEASET Unblocked Bundle, Forced and Gravity Reflood Task Data Report Volume 2, June 1980 Table A-1 Rod T/C Elevation, m (in.) Computer channel 9G 0.305(12) 2 8N 0.610 (24) 5 9G 0.991 (39) 8 8H 1.22 (48) 13 7J 1.83 (72) 59 8K 1.98 (78) 99 11E 2.29(90) 124 8K 2.44 (96) 140 11E 2.82 (111) 155 8H 3.05 (120) 163 9G 3.35(132) 171 8H 3.51 (138) 177 This table provides a legend for interpreting the elevations from the data plots provided in this section. ] l A-2

Table A-2. Run 31203 (3/16/79) Forced Reflood Test A. Run Conditions Upper plenum pressure 0.28 MPa (40 psia) Initial clad temperature at 1.83 m (72 in.) elevation 872 C (1601 F) Rod peak power 2.3kW/m(0.70kW/ft) Flow rate 38.4 mn/s (1.51 in./s) Coolant temperature 52*C (126 F) Bundle radial power profile Uni form Disconnected rods 4G, SG s A-3

== ,Litu,14 414 8 ge.t.C. E,..WE.L,t.,(C.(,S,t. t( 1.f 1, st a roses t tt:( 3 .se attog tes1Tu 1st 11st to.sl 18tse ~ g,g 4 So oa 2 i 250.00 I 40.000 5 / / - 200.00 a b 5 30.000 b 150.N 5 i 20.000 3 E*N r f 3 50. M 10.000 s' i f e 3z s y 0.0 f 0.0 I 4:M -io.000 8 8 8 8 8 8 i i i i i i n ... 1, ~

a 5' 50 ai n..u..,si,.,.,.

.<..,.....a,. , s,i.., ,t ....s .., titi., g,g Cust M

1. 4 II/t lies t Istre g

I

0.000 9

c. 2250.00 d J m 40.000 - 100.00 E150.00 '/ 30.000 S E 5 f u f / 20.000 9 100.00 3 I 10.000 50.000 3 Y z l 0.0 0.0 { y 5 3:M -10.000 z 8 8 8 8 8 8 2 d E I i i i l A-4 \\

Table A-3. Run 31302 (3/21/79) Forced Reflood Test A. Run Conditions Upper plenum pressure 0.'28 MPa (40 psia) Initial clad temperature at 1.83 m (72 in.) elevation 869 C (1597 F) Rod peak power 2.3 kW/m (0.69 kW/ft) Flow rate 76.5 mm/s (3.01 in./s) Coolant temperature 52*C (126 F) Bundle radial power profile Uni fom Disconnected rods 4G, SG, 6J, 11G s ( A-5 b

l l

m 5' a "'

,u c., u su .e. .t...e.u ris, u.it, = Due s a lat,3 stat,reanstra cet,trittger fg,g g (m,1?u t 33 3 ire 8 463,4 g j / /j 50.000 v.: f .M# U g i ) / 'c ~ = 30.000 m i =,,0. h 20.000 3 100.00 / O N u i 3 M.000 - N 10.000 l' g s ( 0.0 0.0 g 7 $*W -to.000 I 8 8 8 8 8 8 8 g s a g g g g a

n...t.o sticar sta$tt vestecato eveou itst steits

I g

e !3,,,,, c.ve,...a s se,t,, star,,f,enestta t.o.t,tricitaf g 3 S o" ,I 3 t i

rso.00

/ L 0.0m { 'f D x 1 = - M.00 [,e-t li ) i;150.00 7 g g l /,./ 20 m 5 .i. ' !...V h f 3,,,, io.0= = a i s 2 0.0 0.0 h 7 I W:M .io.ooo ) 3 8 8 8 8 8 8 8 J 8 R E R 8 8 8 o 2 ~ m TIM i SECOS$$ B A-6

Table A-4 Run 34420 (8/6/79) Forced Reflood Test A. Run Conditions Upper plenum pressure 0.27 MPa (39 psia) Initial clad temperature at 1.83 m (72 in.) elevation 1119'C (2045*F) Rod peak power 2.4 kW/m (0.74 kW/ft) Flow rate 38.9 mm/s (1.53 in./s) Coolant temperature 51 C (124 F) Bundle radial power profile Uni form Disconnected rods 4G, SG, 111J, 121K, 13JK A-7 l

l

M *II

.001 = I,u.,t., u.,u s v.eto.<s a t,e,s et,ies se te,t,,,itige, sie av ess, ustas o so....se e,e,, y,,,,, i u, ..,e g I f i. a

in..

5 .e.000 m - N0.00 3 s' z N.000 !110.00 ( W z k M.000 m j'"" v f~} ,,,0,, .~ i0. - s y i .T g 0.0 0.0 v 5*

ll:ftf

-t0.000 s a s, 8 8 s E E I' R I n...

M 5'

~' ,u.c., u.,u.. v.e.......u,.ri s.,<,u, n..., = es m.m. ae I o {M.00 '"# 5 '" S"# '"# 8 E 50.000 j !250.00 i f ) 1 - n 0.00 / / a 5 f ,J s 1 E 150.00 3 j e 9 }100.00 20.000 y j g j 0,, .0.. T E 4 0.0 V, 0.0 N i -1:!D -10.000 T 8 8 8 8 8

8 2

E E I R I n . =c A-8 7 l

Table A-5. Run 34524 (8/7/79) Forced Reflood Test A. Run Conditions Upper plenum pressure 0.27 MPa (40 psia) Initial clad temperature at 1.83 m (72 in.) elevation 878'C (1612*F) Rod peak power 3.0kW/m(1.0kW/ft) Flow rate 39.9 mm/s (1.57 in./s) Coolant temperature 52*C (125*F) Bundle radial power profile Uni form Disconnected rods 4G, SG, 111JK, 121JK, 13JK 1 I (' A-9 {

" 5' a ai r u,....,......a...n.,.,,.... ...,... i,., u. c, n, I

=

j l i m.= 7 e n f j 'o ~ - n... I l [ / m.= I 5 gin.. m? ) N.0w g w.0m - r a I }/" s-so. m 5I e.e o.a 2 1 i S:M -to.ooo 2 s s s s s s I E A R I

ao 5' a "'

_ u.. u. u.,, ,...,...a,,.,,1.._,u.,..., u .,s. 0.. i,,,. s j M.000 / l 000 l I I - NO.00 3 .J J l 2? l IM.00 g N.000 l 2 10.000 l y 8.0 ,y 0.0 1 1 i I S:M -to.oco s s a s a s 2 N k N N N N I A-10

APPENDIX B FLECSET -- A Computer Program to Calculate Heat Transfer Coefficients During Reflooding B-1

i CONTENTS Page 1. I NTR OD UC T I O N........................... B-3 B-4 2. HEAT TRANSFER CORRELATION.................... 3. THE COMP UTER PROGR AM....................... B-17 4. US ER I NF ORM AT I O N......................... B-18 B -23 5. SAMPLE OUTPUT.......................... 6. C O D E B E NC HM A R K.......................... B-33 7. FLECSET CODE LISTING....................... B -48 8. R EF E R E NC E S.....,...................... B-54 i B-2 \\ -~

1. INTRODUCTION The computer program FLECSET calculates the quench time and heat transfer coefficient for cosine as well.as skewed power shapes. The calculated heat transfer coefficients can be used to calculate fuel rod surface temperature in computer codes like REFL0032 and UPIFLOD' which calculate the primary system behavior during the refill and reflood phases of a postulated loss-of-coolant accioent (LOCA). These correlations were developed by Lee, Wong, Yeh and Hochreiteri by modifying the correlations of Yeh and Lilly and reformulating them in dimerisionless form to provide better agreement with the FLECHT as well as the FLECHT SEASET tests. B-3 1

2. HEAT TRANSFER CORRELATION The original heat transfer correlation of Yeh and Lilly $'0 was derived based on the concept that the heat transfer coefficient is primarily a function of the distance from the quench front, and the basis of this concept has been explained in detail. The correlation predicts the quench time and the heat transfer coefficient quite well for the FLECHT cosine power tests and the skewed power tests with the 15x15 assembly rod bundle. However, the correlation is not in dimensionless form; therefore, it is not general enough to be applicable to other rod bundle geometries such as the 17x17 assembly red bundle of the FLECHT SEASET tests. Lee et al.1 reformulated the correlation of Yeh and Lilly 11 dimensionless form and modified it to provide better agreement with the data of the 15x15 FLECHT cosine power tests'and skewed power tests as well as with the data of the 17x17 FLECHT SEASET tests. This correlation, like its predecessor, consists of two subcorrelations: Quench correlation, which predicts the quench front elevation as a function of time Heat transfer coefficient correlation, which predicts the heat transfer coefficient as a function of the distance from the quench front, I-Z, The heat transfer coefficient can be cceputed as a function of time by using the quench <,orrelation, which bridges the space variable I and the tim + q variable t. The correlations given in this section are obtained from Reference 1 except that they are corrected for errors as given in Reference 4. ) i B-4

2.1. QUENCH CORRELATION The original quench correlation has been modified and reformulated by Lee et al.I in dimensionless form as follows:( i Y { 9 0 "q, peak in ~ 10 +0.5Q e I k ) tV - = 1+ (2-1) Q "It G 1 + 50*1('o-T,,tj where Z Z O (Z) dZ G (Z) dl (2-2) Gr" 0 0 linear power at elevdtion Z of one roc (j/sec-m (Stu/sec-f t)) Q' (Z) = quench elevation [m (f t)) Z = q P"" P"**# 'I'"*EI " b* (It}) Z peak quench time at elevation Z (sec) t = q q fl dl"9 I'C' (*I'*" (f tl#}1 Vin

204 C (400%")

T, = saturation temperature [ C ( F)] T,,gs Whenever confusion is likely to occur, exponentiation is indicateo by**. a. B-5 .,_--4w.,-e-*m_-y.g ,my-w-. -

,_~,_.g.___.,3

--3 ,9,%,,_,y -y, ,-wc-w_p__,,,sg,y-%r, a e--

G'(Z ) q + Tsat, ( C (oF)] (T init-Tsat)O'(Zpeak) Tinit, q 'T cladding temperature at peak power elevation at beginnng of = init flood ( C ( F)] and t is the quench time at the peak power elevation which is given by p,g N g'4 peak = 0.C0019Re (8 /ag) (F I t2 + F ) + (g) + Ft5 3 g t! g 'I I t6

t7 t8 (2-3) where AT

/hfg)) 6.458(10' ) Fgg = exp [- 10.09 (C f sub Rel.938 (,gf,f) 0.5078 (ggopoe/z,,g) 1.5 / p -0.7 {l-exp (-0.0000801 Re/(o /eg)O.262) y g C = 1 + 0.5 exp (- 5.6251 (10 )(,g,,)3) 8 F j g = 1.3 exp (- 1.652 (10) Re jg,g,,)0.524) 2 j F l gg = 17.3 exp (- 5.6251 (10 ) (,g,,)3) 8 l F j exp (- 7.293(10) Re jg, j,,)0.524] 2 I't5 = 66203(o /of)0.2882/Re*I I g -2.8 exp [- 0.000122 Re/(o /og) ]F g t2 'Ft6 = 1.01552 + 0.01388 CT B-6

I 1.05 exp (-0.66 - 0.59 C ) (1 0.5/Cl. 50" Fg7 T = (2-8.137 (10-5) g.f(,gf,f)0.262)) } {pp4} j 1.0 + 0.32 / [1.0 + 50.** (5.0 - 2520.o /o )) F = g f g It8

Ft81 FtS2 0.3 0.7 {l - exp (-10.31(10-8) Re2 (,gf,,)0.524) }

Ft81 = / 2.9 (10-11) Re3 (ag/ofy0.786 exp (-9.3 (10-8) Re2 (,9,,)0.524] f 7 /(! + 50** (- 15.73'(C r 4T,ue/hrg).1.333] } o l-0.16/Cl 70** 1250 (Orod/Z eak) FtS2 = p -5.45 ] / Cl. 80" (7.14 Co - 4.93)] Z 9'*" o(Z) dZ [(a, A,V;n q) C a h g (Tinig - T g)/ (T,,i - Tsat) CT = t water density (kg/m3 (lbm/f t )] 3 of a rod diameters (m (ft}} Orod a flow ares formed by four adjacent rocs (m2(ft )] 2 Ag a latent hest of sysporation (kcal/kg (Stu/lbmil Nfg a t.eidenfrast temperature = 2600C (500cr) T,i = t intet suecocting (OC (Cr}} aT sua 3 i B-7

- _. =- - i The rationale and the method of deriving equations (2-1)and (2-3)are as follows. In the early FLECHT correlation,")the quench time was predicted only for the peak j power elevation. which is 1.83 m (72 in.) for the cosine power shape. In the later ver-lon(5,7)and the present version of the FLECHT correlation, since the concept of the heat transfer coefficient h being a function of the distance from the quench front j Z-Zq was useo, it is necessary to have a correlation which is able to preoict the quench [ time for all elevations. Since the early FLECHT correlation predicts the quench time at the peak power elevation quite well, it is used as a base. correlation in the later and the present versions (equation (2-11 which is denoted by t g ; the quench time of p the other elevations is predicted by adjusting t with the integral of power G ** qpg r I expressed in equation (2-1). in the above correlation, the quench time, t, is given as a function of the quench q elevation, Z. In practice, it is necessary to compute the quench elevation as a q function of time. This can be accomp!!shed by first computing the quench front i velocity, V, for a given time t by (Z + aZ ) - Z 4 4 4 (2-4) V = q t (Z + AZ ) - t (Z ) q q q qq q (Z ) are the quench times computed from equation (8-l'. The y (Z + Z ) and t where t q q q quench front elevation at the time t + at is then computed by I Z (t + at) = Z (t) + V at (2-5) q q i This method of ecmputing the quench elevation as function of time is also valic for variable flooding rates. Note that, for the variable flooding rate case, the actual time t is different from t. (5,7) q 1 B-8 i

It is noted that the power per flow area is preserved in the above correlation through'the parameter C. It is also noted that through the use o,f dimensionless g quench time, t Vq in"q, the length effect (originally f-factor (5,7) has been taken care of automatically. The above quench correlation has been compared with the data of the FLECHT SEASET unblocked test series as well as with the data of the 15x15 FLECHT cosine power test series and skewed power test

series by Lee et al.

In particular, the overlap runs of these three test series have been compared. The overlap tests are the runs which have the same test conditions and the same total energy (the integral of power plus the stored energy) below the peak power elevations, so that the quench time at the peak power elevation is about the same. All these comparisons show that the quench time at the peak power elevation is about the same in each set of the overlap runs, and that the predicted quench times are in good agree-ment with the data. They also showed that the present correlation is in better agreement with data than the prev gus correlations. 2-2. HEAT TRANSFER COEFFICIENT CORRELATION As in all previous FLECHT reports, the heat transfer coefficient is defined as / h=atu al (Trod sat ~ where rod total surf ace heat flux, which includes raciation and convection g,g,g = rod surface (cladding) temperature T = saturation temperature T = The present heat transfer coefficient correlation is diviceo into four parts insteac of three parts:(5) f B-9 1

i l Raciative Heat Transfer perico The radiative heat transfer perico exists only for the case of low initial clacoing For low initial cladding temperature, there is practically no vapor temperature. the lower generation at the beginning of flood because the roos are colo at elevation. Therefore the heat transfer during this perico is essentially raciative heat transfer. Early developing period This period extends from the end of the radiativa heat transfer period to the time when the heat transfer reaches a quasi-steady state (figure 2-1 ). During this developing

perico, the heat transfer mechanism changes from the radiation-dominated prereflood condition to single-phase steam flow.

The me:hanism then changes to dispersed flow when the steam velocity becomes great enough to carry droplets up the bundle. Guasi-steady period During this period the heat transfer is essentially in a quasi-steady state. This m'enns that the heat transfer pattern moves with the quench front; that is, the heat transfer ccefficient versus the distance from the quench front is essentially unchanged with time. Heat transfer coefficient above peak cladding temperature elevation Because the situation above the peak cladding temperature elevation is different from that below the peak cladoing temperature elevation, it must be treateo separately. Above the peak cladding temperature elevation, the steem temperature may be greater than the cladding surface temperature, and the heat may be transferrec from the steam to heater rods. The FLECHT definition of heat transfer coefficient, saturation temperat.ure equal to sink temperature, implies that the heat transfer coefficient is negative. Below the peak claccing temperature elevation, the steam temperature never becomes greater than the cladding surface temperature. Therefore the he transfer coefficient never ~ becomes negative. l B-10 l z

The transition between the radiativG, heat transfer period ano the developing perice occurs when Z is equal to Z and the transition between the cevelecing perice anc g the quasLsteady pertec occurs when Z is equal to Z,, + aZ,, where Z,, ano d, an q computec from the following formulas. The expression of the four-part heat transfer coefficient is as follows: Radiative heat transfer perloc (Zq < Z,g) ~ I"'

I (2-6) hah aC 1-exp p

roc \\ ,r / g where Z is computed from the following dimensionless expression: ac

I ' sue in V

f I = 0.852 o GInaxA ad 8 }'*d(T "I" T** v Z I I" M { -0.234 + SaxA ad and 2 9 2,g ) / 36C0.0 (36745 J/ C 7,2(0.215 Stu/ 2 j C = heat capacity of a rod (j/m-QC (Stu/f t.0F)] (8C Alrod a p l c-(Z) gngg. T,,g)G'(Z,,,g) (T T nitz = i 371 "C (700*F') T,, a 224*C (4359) AT, a heet capacity of water in a enannet fermec my four aciacent rocs (aC, A), a (j/m *C (Stu/ft I)] 0.3496 m (1.147 ft) Z, = 2 hest transfer coefficient (1/sec *C.m2(Stu/see Y f t ) n = 1/ 1 + 70** (1-0.0133 (Z,,,,/Ow,)]f r = n i 8-n

given by equation (2-6)is mainly It is noted that the radiative heat transfer coefficient hg due to the radiative heat exchange between the rod of interest and its neignect:ng thimble and rods. Therefore, h aspends on the temperature difference eetween tne g rods and the neighboring thimbles. The temperature difference cepenas en tne pre-reflood hestup rate. For example, if the pre-reflood hestup rate is very slow, enen the radial temperature will be essentially uniform and the temperature onfference l practically zero,'so that h is also zero. Tt)e faster the heatuo rate, the larger tne g J temperature difference and hence the larger the h. This mechanism has been oiscussec g in great Isogth in WCAP-7931.IE The heatuo rate is proportional to tne local power G"I; This teacs to and la inversely proportional to the heat capacity (a C, A),,, of the rod. the expression of equation (2-6). s Developing period (Zad

A #I
# s) q ad g (1 - exp (2.5x - 101, (Nu - Nu 3(1 - exp (2.5x - 10)])

Nu = Nu 2 2 (1 - e*

0.9 x e' * )

(2-8) 9'8 where Nu a h O N*

Iad
N '

red g q s developing period to the quasi-steady period, where AZ,is computec from = 6329 (Re. 4000T

"'8 F (24)

I h 2Ob 8 in fp s g l Other parameters are computed as follows t l Ng a Nu.108 exo (-iJ3(10*b Re/(e /of)0262) y g (2-10) exp (-0.0534 (Z - Z )/0,] q g anc g, respectively, tnen using the and Nu) are cornputed by first calculating h Nu g definition of the Nusselt numeer sa follows frorn equation (S-6) h a g g g 0,/k Nu g h g B-12 l

T h)(lgf,7 - T,,,) D =1.21 1 - exp -3.05(10-5 ) Re(o of)# rod l "aff,Z (2-11) 0.714 + 0.286 1 - exp (-3.05(10 )(o /pg )l.524 -2 Re ) g Nu)=h)Ogk The other parameters in the above correlation are i

- ' )

[T -T ~ I"IE ? I + 60** 1.08 -1.26 AT, AT,gg = ( ) c 427 C(800%) AT, = = Tinit + AT,gg eff Q'(Z ) 4 T,gg,7 T,,g+ (T,,, - T,,g ) = G,(Zpeak) 4 (Z - Z,,)/aZ, x = q hydraulic diameter of channel formed by four adjacent roos (m (ft)] De = density of water at saturation temperature (kg/m (lbm/ft )] = og 3 density of steam at saturation temperature (kg/m (lbm/ft )] o = g specific heat of water at saturation temperature (j/kg-C C a pg (Stu/lbm Y)] conductivity of water at saturation temperature k = g (j/sec-C-m (Stu/sec-Y-ft)] j 2297 w/m = 2297 J/sec-m (0.7 kw/f t) Q',g f = \\ Q',gg Q'(Z )/Q'(Z sk) Q',gf = q B-13

conductivity of steam at saturation temperature k = (j/sec-C-m (Btu /sec-F-ft)] rod diameter [m (f t)] D w rod V U/eW Re = of in , Quasi-steady period (Z >Zad

AA }

q s Nu = Nu 2 Above peak elevation (Z > Z,g) p O Nu = Nug - 44.2 1g7 exp -0.00304 (Z - I,y/0, p peak-where Nu = Nu for radiative heat transfer period, Nu = equation (2-8) g g g f r quai-steady periode developing period, and Nu4 = Nu2 it should be noted that, in the above correlation, all expressions are in dimetuionless forms except equation (2-6),which is primarily due to the radiation. Therefore consistent units must be used. The above correlations are valid over the following range of parameters Pressure (P) 103 - 414 kPa (15 - 60 psia) Inlet subcoeling (ATg) 9 C - 78 C (16 F - 140Y) Initial temperature (Tinid 149 C - 1204"C (300Y - 2200 F) Flooding rate (Vg) 1.02 - 25.4 cm/sec (0.4 - 10 in./sec) Equivalent peak power (Q' max, eg) 0.984 - 6.56 kw/m (0.3 - 2 kw/f t) b where the equivalent peak power is the power equivalent to the peak power of the f FLECHT cosine power shape when the integrated power is preserved. That is,

I

( "Zpeak O'(Z) \\ peak ) C 5 Apes) FLECHT cosine bax, eq * (*O ,0 1 peak G'(Z) fI peak G'(Z) ) Z e s l T cosine O O'(heak max > 0 I peak} In, terms of dimensionless parameters, the above range of parameters can be written as Z 0.204 - 1.14 '( ! I ^I I"hy C = g 0 4 1 M - 6.9 sat) / (T,$ - T,,g). T,= (T -T C g init 0.000636 - 0.0036 o /of g 0.0165 - 0.158 (C AT3gg / h g g y 9 470 - 8620 V O I "f., Re = of in e 61 - 284 2 IO pak rod It is also noted that the dominating term in equation (2-3)of the quench correlation is The next dominating term is the brace the first term in the expression for Fd. containing parameter C in W expmssim for Fgg. The third dominating term is the g brace containing AT in expnss e f r Fgg. As for the heat transfer coefficient SUB correlation, since the expressiens are quite simple, nothing can be said about dominating terms. 8 i I B-15 j i

1 - RADIATIVE HEAT TRANSFER PERIOD H - DEVELOPING PERIOD l III - QUASI STEADY PERIOD g h i I i l I I h - 8 I l l t l i i I i I I I l u Z l l COLD FILL g i l i l i I I I I i z I l a i I I i i I i Z g +.1 Z s Z g t Tq f Figure 2-1. Adiabatic, Developing, and Quasi-Steady Periods in Heat Transfer Coefficient Correlation B-16

3. COMPUTER PROGRAM A computer program FLECSET is written to solve the equations given in Section 2. Major part of the program is taken directly from the computer program given in Roference 1 with minor corrections as given in Reference 4. The program can be run on CDC 7606 computer. The geometry and power informations and the axial location where the heat transfer coefficient is to be calculated are input by the user. The water and steam properties are calculated using STP' library. The results printed out are: quench time, heat transfer coefficient, H, quench height, ZQ, the quench front velocity VQ, and the core inlet velocity, VIN. A plot capability is added to the program so that two plots, heat transfer coefficient vs. time and quench height vs. time, will be obtained. The user information and sample output are given in Section 4 and 5, respectively. A copy of the listing of the computer program is given in Section 7 O B-17

4. USFR INFORMATION l

4,1. Input The input to FLECSET consists of eight cards, the last four of which are multiple cards to input tables. All tables should be input with increasing values for the independent variable (first variable in the card). Card 1: (Fomat 4F10.5, IS) DTSUB = degree of subcooling associated with the water entering the care, 'F. P = system pressure at end of adiabatic heat up (E0AH), psia TINIT = Initial cladding temperature at E0AH, *F PWFT = Design peak linear heat power rate for the elevation of a particular power shape. KW/ft. MR = 1 for FLECHT radial power shape 2 unifom power shape (radial) Card 2: (Fomat 5F10.5, F10.8) Z = Axial position (ft from inlet) ZDBUG = 0 (if set >0 ft it prints out additional infomation useful for debug Q/A purposes) ZPEAK = Peak Temperature Elevation (ft) DR = rod diameter (ft) DE = hydraulic diameter of channel fomed by four adja' cent rods (ft) 2 A = flow area fomed by four adjacent rods (ft ) Card 3: (Format 3F10.8) POP 0X = P/Po factor at the end of adiabatic heat up (Q',x = PWFT x POP 0X) RCPAF = (oC A) for the water (BTU /ft-F) p RCPAR = (oCpA) for rod (BTU /ft-F) B-18

Card 4: (Format 4Il0) NVIN = number of cards for the inlet velocity table (card 5), maximum 100. j NDECAY = number of cards for nomalized pcwer decay (card 6), maximum 100. h1NTPR = number of cards for nomalized integral of power (card 7), maximum 100. NPSHAPE = number of cards for axial power shape factor (card 8), maximum 100. Card 5: (Format 2F10.5), maximum No. = 100 VINTM(J) = time, seconds VINTB(J) = flooding rate from reflood, in./sec. Card 6: (Fomat 2F10.5), maximum No. = 100 PDCT(J) = time,tj, seconds , t) CI'(Z.t) dt PDCAY(J) = o' CI'(Z,0) tJdC'(Z,t)dt o O'(I,0) decay curve B (Figure 1) 4 where the nomalized R.ECHT power decay curve is shown in Figure 1 (Figure I-1, Reference 1). A table of PDCAY for ANS + 20% power decay is given in Table 1 ( (page I-6, Reference 1). l Card 7: (Format 2F10.5) maximum no. = 100 QAxZQ(J) = axial location Z)(ft) ,Z) QAXTB(J) = Q' Z,0)/Q' y dZ = integral of axial power nomalized using the maximum power. L / Card 8: (Fomat 2F10.5), maximum no. = 100 ) FAXZ(J) = axial elevation Z)(ft) FAXTB(J) = Q'(Zj,0)/Q' max = the axial power nomalized using the peak power B-19

4.2. Output Yime = time to reach the quench front to certain elevation Zq, seconds (This time is equal to the actual time as long as the cuench front propogates from the bottom to top) 2 H = heat transfer coefficient at a given height Z, BTU /hr-ft -F and also in 2 i W/m -C 1 ZQ = quench front elevation, ft, and also in m. VQ = quench front velocity, in/sec. VIN = inlet flooding rate at the output time, in/sec. j l I B-20 L

s TABLE 4-1 Table of Nomalized Power Decay 1 t C'(Z t?dt PDCAY = od ( '(I.0? t "7C'CZ.t? 1 dt f C L,Z,0 D FLECHT DECAY CURVE This is the normalized power decay relative to the nomalized power decay used in FLECHT experiment. The FLECHT decay curve is shown in Figure 4-1. ANS + 20% power decay is used in FLECHT-SEASET tests. The PDCAY for this.ANS + 20% decay are given below. PDCT(J) PDCAY(J) (sec) (-) 0.00000 1.00000 20.00000 1.08500 40.00000 1.15300 60.00000 1.19800 80.00000 1.22600 100.00000 1.24400 120.00000 1.25500 140.00000 1.26200 160.00000 1.27000 200.00000 1.28000 280.00000 1.29800 360.00000 1.31100 440.00000 1.31900 520.00000 1.32400 600.00000 1.32700 I 680.00000 1.32800 2000.00000 1.33000 B-21

o D R 3 C 3 8 i ~ e E 3e h ~ e 3 a E o Z 8 o e e o U a b N U w l t a ~ t W Q 2 o 8 N c. 2" O W 8 a w T I I I i l i o 8 o e a v. e a w n n ~ o 5 a 6 6 6 6 6 6 6 6 6 6 (O'Z),01/(1'Z).O 'W3 mod 032I1VWWON O B-22

5. Sample Output i A copy of sample print out is given in Section 5.1.5, and the sample plots are given in Figures 5-1 and 5-2. 5.1. Sample Printout CA A0 IMAGt LI3TIMG 1234579k!kkkhahNk!!!!fh ! $12 Seh.IIZ$I 5 .9 2 5" a'" til;;,.,:!il... ;l:::;;j lit' ahih litt !L:t i:!ti ta i:iH1 l:lL:l s:LIn llp3(1 1:!41 1 .il:1 i:!M 'i! ', al{.l;ll g3.Wi ! :1 L:11

l: I.l.s i...

i.

13 1:111

?? !:'!t f:I 9: 2:gj!!

7. 3 S.

4 1::i' 1:111 ill:'I j::til t Sil: u ih{ f:ff L: '.t. !!:i ! L:j){ n;I"! L: S 2:1). 1:tt{ L: I:!4. \\ B-23 ,,-~--.n,__r-,w.,,

j s I l ) CA.9 I R A,G E L!37ING in.. 7.,illiHHuillitiH.4.g!g g M M1..if..12:4u8; g NUM B

t.t.

1I u:4,:.-

f:1 I:l.l. u:!:i.?

7..

~.. r r ..g .7. l:2 L: l Ul:l

:S L:

P:tf l1:*h 4

lH:i' H:i

- - E N O OF INPUT L I$T ING*

.!!!!!all .:4:llia.. .I!!!is!!... D iisil'n "I ..Z.t F.T..)... e t ZD.UGipft ..Z,l A.u..f.p f..l . 2 217.f.l -.i De t P i . 2..lp f.3DE.. c-i..a.t F. T 2 3.-. 2 ..O M.M.f = )E=.1 P .C .CPA .S PAS..E=.1 .J4 5.R..E=.1 177 J vig Cg ar rg si.,g TA.Lt OF TIME VS WIN FINE V!M(IN#33 ,,1: lit:1

11:18 B-24

i s w TA8LE OF NORM.LIZE0 POWER DECAY TIME POCAY 23...... i...... 4......Q J. L...S.. 1.153.. it:Ill! ill:l.!!Il i:)1lIl i lli i:2}!n .!!1:llaii !:{ilil r {ti:lll11 i!:!!!n 1: Il i:B*ul 111:11. t:iTill aill:llitt i:lilli McAMALIZIO INTEGRAL OF POWER J MEIGMftPT) GAXT OS ..5.111 :Mlll' .. u a A ):1 3:lilli i:ltill

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t i TSAfs267 316391 VO L F=. 01714433 v0 lgs 10 5818222 K Gm.80880453 VISCa.0001414 CPFe 1.0190444 MF. 236 2* *30 NGe1178 83427 KF= .0081099 .......e. ) THE SESULTS OF THIS TEST CSSE 2e 4.08008 FT l eeeeee eeeeeeeee ee eee I TIME N 20(FT) N(3 !I 20(M) VQt!N/$) VIN (IN/53 J !OTU/MA-FT2 7) 0.48888 3.2852 .88508 18.4542 .001S2 .47185 .40848 2 54529 3.2852 .10000 18.4542 .83048 .47114 .48808 S.89317 3.2852 .20008 18.4542 .04494 47891 .48800 7.44085 3.2852 .38888 18.4542 .09144 .4712' .40800 l } 10 18553 3.2852

.40008 17 4542

.12192 .47200 .48000 '12.72442

3.2852

'.58888 18.4542 -.15248 .47332 .40088 15 25448 3.2852 <.4880s 18.4542 .18284 .47515 .4000s l 17.77400 3.3250 '.78888 18.4804 .21334 .47750 .40008 28.27875 3.9447 .48800 28 1275 .24354 .48123 .48888 22.74202 4 2lt24 .90890 24.8344 .27432 44444 .40800 25.22709 S.1$89 1.88888 29.4442 .38488 .44817 .40008 27.44925 6 8939 1 14888-34 37S4 .33928 .41363 .40008 38.88714 6.4472 1.20888 37.7445 .34576 .49881 .40000 ( 32 4787. 4 9933 1.30000 39.7098 .39424 .50452 .40008 34.84213 7.1882 1.44800 48.4167 .42672 .51075 .88808 f 37.17542 7.3065 1.58484 41 4479 .45728 .51751 .40800 39 47743 7.3495 1.,41800' 41 9345 .48744 .52479 .40008 41.73764 7.+404 1 78004 42.2483 .51814 .53S44 .80088 l 43.96815 7.4765 1 88805 42 4534 .54444 .54404 .80000 18 90980 7.6347 1 10808 43.3433 .57912 .36449 .40808 ,jj $4 15314 7.4578 2.00ste 43.4828 .48948 .37384 .4080s l- $7.32009 7.4819 2.10888 43.4201 .4 40 B4 .J8343 .40000 40.48447 7.7897 2.20004' 43.7777 .47056 .39974 .40000 l l 43531341 7.7414 2.38880 43 9987 .70184 .44449 .4880s j l ~ i + B-26 i / I

78.71828 7.7782 2.48888 44 1445 .73152 .29748 .40000 74.64499 7.4282 2.58888 44.4851 .76208 .38464 .48888 78.48E94 7.4644 2.40888 44.6798 .79244 .32814 .50800 42.14482 7 9238 2.78088 44.9934 .42296 .33326 .40000 45.44264 7.947S 2.48888 45.3548 .45344 .34495 .84800 l 89.18234 4 8485 2.90000 45.7694 .44392 .35429 .40000 12.41757 4.1444 3.88888 44 2459 .91440 .34704 .40808 188.71931 4.2487 3 18888 44.7927 .94484 .24906 .40008 104 48986 8.3513 3.28888 47.4287 .97536 .29716 .48888 188.48881 8.4782 1.38080 44 1417 1 08544 .38362 .40888 112.71494 8 6248. 3.40480 44 9496 1 03632 .38827 .48808 114 59148 8.7915 3.58088 49.9202 1.86488 .31185 .48088 123.67418 4 9837 3.68888 S1 8114 1 89728 .26438 .40000 128.21957 9.2844 3.70008 "**S2.2652 1 12776 .24342 .48800 132.79844 9.4579 3.40888 S3 7844 1 15824 .26133 .48088 137.41293 9.7449 3.90884

55.3569 1.18872

.25789 .40008 142.12842 10 8431 4.88888 57.2544 1.21928 .25344 .40000 144 48941 18.4444 4 18880 59.4332 1.24944 .24473 .40888 155.44488 18 9874 4 28888 61.1351 1.28816 .20358 .88800 141 84451 11 4133 4.30000 64.4874 1.31064 .19934 .80808 167.13741 11.9942 4.48888 64 1863 1.34112 .19493 .40888 173.36292 12 6413 4.S8088 71.4939 1 37144 .19844 .48888 179.71418 13.4272 4.44888 76.2524) 1.48288 .14727 .40000 184 18834 14 3046 4.70884 41 2347 1 43254 .14413 .48808 192.74487 15.3165 4.80888 84.S708 1.44304 .18144 .48880 201.59639 14.4768 4 98888 93.5549 1 49352 .16988 .14000 208.73584 17.4874 S.38888 181 1151 1.52488 .16727 .40888 215.94358 19.3342 S.18008 189.7948 1.59444 .16588 .40000 223.28841 21 8916 S.20804 119.7439 1.58496 .16444 .48888 O { B-27

l l 238.51988 23.1973 5.30888 131.2094 1.61544 .16372 .80000 237.86496 25 4214 S.48888 144.351? 1 64592 .16300 .8800d 244.78593 28.0794 5.50880 159 4422 1 67648 .15383 .80000 254.63928 31 1310 5.40000 176 7498 1.72680 .15261 .80000 262.51117 34.6349

5.70088 194.4462 1.73734

.15230 .40000 270.39718 38.4583 5.80080 219 5121 1 76784 .15206 .88000 278 21481 43.2782 5.98080 245.7448 1.79832 .15188 .40000 284 18463 48.5829 4.00008 275 8463 1.82880 .15284 .88000 294.88026 54 4748 6.10800 310.4532 1 85128 .15194 .48003 301 94049 41.e481 6.28888 350.1674 1 88976 .15186 .40000 389 88452 49 6990 6.30088 395.7691 1 12024 .15179 .40008 317.71179 78.9205-4.48000 448.1389, 1 15072 .15173 .80000 325.78113 49.5898 6.58085 508.2552 1.98120 .15168 - .80000 331 85551 101 6672 6.48000 577.2925 2.31168 .14815 .80000 339.31260 113 6277 6.70000 "*$56.5443 2.04216 .16890 .80E00 ~ 344.77181 131.6579 6.80000 747.5877 2.47264 .16885 .40E00 354 23308 155.0644 6 98088 852.1049 2.10312 .16881 .80000 361 68882 171.1997 7.00005 972 1141 2 13360 .16117 .8000n 349 13528 195.4681 7.10808 1109.1185 2.16488 .16114 .40080 372.45228 223.3341 7.20088 1268.1493 2.19456 .17879 .48800 379 47946 255.3312 7.3,0888 1449 837B 2.22584 .17876 .88008 386 78693 292.8717 7.48888 1654.4590 2.25552 .17874 .40000 393.73589 334.2587 7.58088 1198.8881 2.26600 .17071 .40000 488.76593 382.6994 7.44800 2173.8491 2.31648 .17868 .48080 487.79785 438.3228 7.78888 2488 9865 2.34696 .17066 .80000 414.82926 542 1980 7.80000 2851.5451 2.37744 .17863

80000 412.31376 575.5260 7.90888 3267.1848 2 48792

.20411 .40008 417.89331 659.7334 8.00808 3746.1392 2.43840 .20408 .80000 423.77362 756 4247 8 10008 4295.1761 2 66888 .20404 .40888 I i B-28 I

.. _ = l 429 45444 447.4497 8 20004 4925.4844 2.49934 .28483 .58800 435.53451 994 9335 4.38088 5449 4914.2.52984 .25401 .48000

41.41278 1141.3142 8.44800 4448.4903 2 54032

.20435 .40800 434 89947 1389.3994 8.50088* 7435 1183 2 59088 .24134 .80808 439 86444 158244088 4 48088 8531.2188 2.42128 .24177 .40038 444.83234 1724 0120 S.70400 9789.3444 2 45176 .24175 .setes 448 99424 1978.4764 8.40808 11234.3854 2 44224 .24174 .40000 453 94847 2270.4447 8 98000 12893.4244 2.71272 .24172 .40088 454.92508 2464 1479 1 86s00 14798.4989 2.74328 .24171 .48480 440.22184 2991 4877 1 19888 14945.1989 2 77344 .31821 .48800 443.99389 3433.7974 9.28888 19497.7672 2.88416 .31419 .40000 447.74443 3941 4431' 9.38848 22381.9813 2.43444 .31818 .48888 451 53400 4924 9041 1 48088 25493.5934 2.46512 .31816 .88000 455.34775 5194 5449 9 58'888 't9494 2264 2.89960 .31815 .40008 499.37970 5963.5488 9 44888 33,442.5806 2.92004 .31813 .4880s 433.S4370 6444 5038 9 70088 34476.2239 2.95454 .44434 .40800 434.25948 7448.3545 9.88008 44433 1134 2.94784 .44913 .48584 438 92734 9624.4957 9 90800 51243.4329 3.81752 .44911 .40000 441.S9934 18341.2194 10 88886 S4833.4975 3.34408 44918 .80000 444 27142 11894 1854 10 18888 47S49 1794 3.87848 .44904 .40000 403 44142 13458.5384 10.28880 77554.4444 3.18894 .44177 .40000 485.44159 15442.2257 18.38880 89047.7544 3.13944 .48174 .80000 407 14143 18885 9234 18.48888 it22?2 3143 ~3.16992 .44171 .40088 484.92213 20674 8972 18.50000 117392.4949 3.28844 .68169 .80000 418.44258 23737.4139 18.68888 134789.4792 3.23844 .68164 .40000 412 44294 27255.7188 13 70808 134765.8124 3.26134 .68164 .40C88 414 2934$ 31295 1177 18.488td 177781.4149 3.29144 .64141 .48800 415 94403 35933.3497 18.*1080 204038.4796 3.32232 .48154 .40040 417.72447 41259.1678 11.88888 234288.2777 3.35280 .44156 .40008 i l l s j B-29

419.48538 67374 5137 11.10000 269004.8044 3.38328 .60153 .80000 421.24614 54396.4289 11.20000 308877.0645 3.41376 .48150 .80000 423.00701 62459.3067 11.30000 354660.1827 3.44424 .68148 .80000 424.76793 71717.4643 11.40000 407230.4087 3.47472 .68145 .80000 426.52891 82348.0954 11.50000 467593.8984 3 50520 .68142 .80000 428.28996 94554.6633 11.60000 534905.9627 3.535e8 .68148 .80000 430.05108 108570 7913 11 70000 614493.1815 3.56616 .44137 .80808 431.80925 124644.7376 11.80000 707478.7932 3.59664 .68258 .80000 433.56731 143144 5231 11.90000 812811 8484 3.42712 .46256 .80000 435.32540 164343 851.9 12.00000 933300.6854 3.65760 .68255 .80000 40 07 CALCULA7 TOM ***** O 4

l 67.200. ' 39 288-P = 40 psia ( = 0.7 kw/ft ATsub " 1 si.sco. Tinit " v, = 0.8 in/sec i Z e 6 ft +3. mas _ k t i 2s.mo. B E Y 27.200 t9. toe.

ace _

3.2co 0 000 $.aao id. asp M.aso 32 000 4e.0o0 4s.oso riertxio ) HERT TRAN CORR t ( FIGURE 5-1. Heat Transfer coefficient vs. Time j B-31

18.o00 P = 40 psia as.ao0 hx=0.7kw/ft ATsub = 1 F I 2.01M. T = 1600*F init vin = 0.s in/see to.ono-Z = 6 ft C ) 6 a.oso. E e.aaa. 4.deo_ 2.000

a. m 0.Co0

$.000 16 000 2t.000 32.000 40 000 4t. coo 1 TIN (Xio 8) QUENCH HEIGHT i f FIGURE 5-2. Quench Height Vs. Quench Time B-32 l 1

6. CODE BENCHMARK The purpose of the FLECSET computer code benchmark is to show that the predicted results agree reasonably well with the experimental results reported in Reference 1. Lee et al.' have made an extension comparison study between the correlation (predicted) results and the measured results of FLECHT SEASET experiments. Thei r predicted results have agreed reasonably well with the measured values. They have also shown that the present correlation gives better comparison with the WCAP-9183 and WCAP-8838 data than the previous correlations given in these reports. Comparison of the present correlation with some of the' boiling water reactor (BWR) 0 I FLECHT data and Semiscale test data have also 'been made by them with reasonably good agreement. In the present study, nine test cases were selected from Reference 1 covering the wide range of variables used in their experiment. The FLECSET code run ID, the experimental test run ID and the test conditions for these nine test cases are given in Table 6-1. Figures 6-1 through 6-9 show that the predicted heat transfer coefficient and quench elevation vs. quench time agree well with the experimental results. Two additional test runs were also made using the typical input values, varia-ble flooding rates, and skewed power shapes with peak power values at 8 feet and 10 feet, respectively, from the bottom of the core. The FLECSET code run ID and the initial conditions for these two test cases are also given in Table 6-1. Figures 6-10 and 6-11 give the predicted heat transfer coefficient and quench height versus time for these two test cases. From these results it can be concluded that FLECSET code can be used, with confidence, to calculate the core heat transfer coefficient values during the reflood phase of a postulated loss of coolant accident (LOCA). k j B-33 I

l ~ 0 Y - 8 l 8 2 3 e 2 2 I 1 e _1 i g G N H N - s _N l 7s a .I P e c n er 3 l 3 g g 3 1 3 2 2. e 1 1 f a e r m R o k e a 0 s. 0 4 9 0 e. 0 o et 8 d pi o E 8 0 4 8 6 6 6 C 8 o C J = 1 i 1 1 1 q re E t u e p r m u o sa C sl 8 9 8 0 0 0 0 0 3 3 ee 4 2 4 4 4 6 4 4 4 1 rp 7 A P SC E. n t i r l top 8 2 1 9 t t 5 8 5 5 g eomT 4 t 3 4 3 e e 4 4 1 1 l ce 8 i 1 1 1 l l 1 1 n nbT' i t I u r s a g u l n g ae gu iT 0 1 6 0 0 0 0 0 9 s t T 0 0 1 1 ) 0 0 0 0 0 9 id' 6 6 6 4 I 6 6 6 6 6 6 1 e na 1 i 1 5 I 1 1 8 1 1 s Il s C a C gn e a I t l k i c b h 8 5 5 8 8 0 "f r dee 5 e A e a ot s l 1 O n oa/ 8 0 1 1 6 8 l r t u lpn l e a c F i n I V Y e s 5 3 1 0 1 1 1 1 1 8 1 1 1 1 1 rt 0 9 kef 6 aw/ e 4 0 8 4 4 0 4 9 1 eow 0 0 E PPE ts A I re e d d d e e e e d d ep e e e e n n n n e e wa w w w w w l t l l w u oi e e e e o s o e o s n n. PS k t k k k o o o o h C S s s s s C C C_ 5 S 5 5 1 l 7 1 1 2 1_ 1 I S 1 8 1 I 1 1 1 e a_ l e m a m m n m a m a dp ny 5 s S 5 5 i I 1 1 1 1 1 uT 1 i S 1 8 l I 1 1 1 B r 3 0 6 2 1 3 4 ) e 0 5 1 2 4 3 8 ) teb 3 ) 8 0 8 1 9 1 3 ssm 3 s 6 2 6 1 2 5 2 eau 1 i 3 1 3 3 3 3 3 TCN L L C Q a A Y C R I s D. e C D E N 4 U V T ,A J F F F D D A t A n 8 E A A A A A A l A ^ m A E E T E E N A E = n s D D P D D D C D n u D S A i A A A A A A A A a a e 2 3 4 S 6 1 a 9 e l 1 s l I s yw f 1 i'

1 l ok ~ oo o 10 O ~' ~ CORRELATION y 5,a= 8 A ~ DATA W o gy'RUN i 13303 = PRISWRE = 41 PSI A g PEAK P6WER = 0.7 KW/FT e 2 7 FL000lli6 RATE = 1.5 IN/SEC p" INLET W BC00 LING = 141*F IglTI AL plAD TpIP = /600*F, 0 / 0 50 100 150 20 30 300 350 110 0 450 ~ Quench time (see) C RUN f 13303 "g PRESSURE a gi ps A i PEAK POWER = 0.7 RW/FT h i 4 50 - FLOODING RATE = 1.5 IN/SEC INLET SUSC00 LING = 141*F l I t O INITIAL CLAD TEMP = 1600*F F' Z = Z,,g a 10.0 FT. It I r

a MD 76

- --- - ROD 56 3 2 --- n00 5F

g

% -CORRELATION 9.y n 10

%2 i i i i 0 100' 30 20 WO 500 Time (sec) Figure 6-1. Quench Correlation and Heat Transfer Coefficient Versus Data, Skewed Power Run #13303 I B-35

l2 \\ ase ,M ' ax, -cans 10 -m '" h O CORRELATION DATA ~ a ~ fPRES$URE = 110 PSI A ~ G cpr PEAK POWER a 0.7 KW/fI FLOODING RATE = 0.8 IN/SEC p, g INLET SUBC00 LING = 140*F 9" INITI AL CLAD TEMP. = 1600*F 2 aur' ELEVATION = 10 FT. e 0 0 t00 20 300 160 0 500 600 700 Quenchtime(sec) C l PitESSURE = 110 PSI A J

,e O'

PEAK power = 0.7 KW/FT. i 80 FLOODING llATE = 0.8 IN/!EC 4 INLET SUBC00Lill6 = 1110'F s' INITIAL OLA0 TEMP = 1603*F ,e' 50 3 110 fJ ROC 76 s' R00 56 j I3 3 Noo its j 20 ELEVATION = 10 FT. E. O 10 = 0-0 100 20 300 110 0 500 000 700 800 Tlee (see) s Figure 6-2. Quench Correlation and Heat Transfer Coefficient Ver' sus Data, Skewed Power Run #153L5

l RUN i 16110 12 PRESSURE = E PSI A m PEAK POWER = 0.7 KW/FT _ 10 FLOODING RATE = 0.8 IN/3EC ~ F "q INLET SUSC00 LIM = 132*F g 8 INITIAL CLA0 TEMP = 1617'F,{,' OATA g ELDATION = 10 FT. 7 s!6 Q' CORRELATION c .,e 5 GD $' / 2 as/ S'# I e i I t i e e t i t O 100 30 300 @ 500 000 700 800 900 1000 Quench time (see) O EUR i 18110 PRESSURE = 20 P3tA } 00 " PEAK POWER = 0.7 EW/FT f, FLOODING RATE = 0.8 IN/SEC. 50 INLET SUBC00 LING = 132*F INITI AL CLA0 TEMP = 1617'F l ELDATION = 10 FT. i'

I W l

9,f 2 $ 30 R00 5F CORRELATION / 3 --- - neo a6 i f R00 44 .V %g 3 3 r {lo 31-w ^rg_ e - 0 1 0 100 30 300 1100 500 000 700 800 900 1000 Time (sec) Figure 6-3. Quench Correlation and Heat Transfer Coefficient Versus Data, Skewed Power Run #16110 k b-37

~ i2 o o #6a,'o oe o co s o o cm 10 o o gr oocnemma - co ao e' ~ CORRELATION \\e,'oco-e-- DATA E 4 gm 5 o ape./ 6 PRES $URE = 40 PSI A ,A PEAK POWER = 0.7 KW/FT FLOODING RATE = 1.5 IN/SEC ay[ INLET SUSC00 LING = 141*F INITIAL CLAD TB4P = 507'F 2 g ELDATION = 10 FT. h f 0 0 .50 100 150 20 250 300 350 Quench time (see) O / 000 5F 0 j 50 - - - 200 76 i 9 g 3 ELDATION = 10 FT. CORRELATION M O 40 4 1 o l xm 7 PRES 3URE = to PSIA d PEAR POWER = 0.7 KW/FT 8 ~ w FLOODING RATE = 1.5 IN/SEC litLET SUSC00 LING = 141*F t 3 10 A j IRITIAL CLAD TDer = 507*F _s i i i i i i i 3 0 0 50 100 150 20 250 300 350 400 Time (sec) Figure 6-4. Quench Correlation and Heat Transfer Coefficient Versus Data, Skewed Power Run #12816 B-38

I2 o o oc o asom o gA, e o-10 o$ mo ~ o o / em CORRELATION - _/ p DATA _e com 8 / 3 o, / cm:n 4 = C, PRES 3URE = 40 PSI A p. PEAK POWER.= 1.0 KW/FT 4 FLOODING RATE = 1.5 IN/SEC INLET SUSCO3 LING = 130*F 2 INITIAL CL A0 TD4P = 1636*F ELEVAT10ll = 10 FT. ,as O' 0 100 20 300 110 0 500 000 Quenen time (see) 61.44 g PRESSURE = 110 PSI A 4 A PEAK POWER = 1 KW/FT. i FLOODING RATE = 1.5 IN/SEC. O 50 1 INLET SUSC00 LING = 139'F INITI AL CLAD TDIP = 1434*F I l $ 110 ELEVATION = 10 FT. f ~ CORRELAtl0N / }m t 2 i Mf' }" m. }

i..

--- R00 SF ~ 10 .f e w a l 0 L 3 0 100 30 300 110 0 500 600 Time (see) Figure 6-5. Quench Correlation and Heat Transfer Coefficient Versus Data, Skewed Power Run #16022 B-39

I2 D

10 oo 0

sCD 8 8 MTA y 3 o e E PRESSURE = 4 PSIA M PEAK POWER = 0.7 KW/FT g 4 FLOODING RATE = 4 IN/SEC NEAT SU8C00 LING = 190*F 4 f INLET CLAD TDIP = 1600*F ~ CORRELATION ELEVATION = 6 FT. s 2 P Ca 0 25 50 75 100 1 25 I50 175 30 bench time (sec) C PRES 3URE = 40. PSIA

- 70 9

PEAK POWElt = 0.7 KW/FT i g FLOODING RATE = 6 IN/SEC O 1 40 e INLET SUSC00 LING = 140*F 4 lillTI AL CLAD Til4P = 1600*F" A ELEVATION = 6 FT. 50 =f# '7 N00 10N ~~

200 7J j

- 200 7s / -1H*- CORRELATION g l }10 l l 3 0' 0 50 100 150 200 250 Time ( sec) Figure 6-6. Quench Correlation and Heat Transfer Coefficient Versus Data, Cosine Power Ft.ECHT SEASET Run #31701 B-40

12 c S.,\\ cp gto o 52D CP ~ gip i =FF $4 o ELEVATION = 6 FT. PRESSURE = 00 PSI A PEAK POWER = 0.7 KW/FT ~ O FL000 LNG RATE = l lN/SEC CORRELATION INLET SUSC00 LING = l 40*F 2 INITIAL CLA0 TDIF. = 1600* F 0 i i i i 0 100 30 50 110 0 500 600 Quench time (see) C "g 300 1011 j 1 00 ... N00 76 s 4 -. _ 200 7J . $ 50 -, pCORRELATION ' l ELEVATICII = 6 FT.h lg 8 En f ;s N CORRF.LAtl0Il .2 s / / PRESSURE = to PSIA ~ PEAK POWER = 0.7 EW/FT s + FLOODING llATE = 1 IN/SEC g3 l [/ INLET SUSC00 LING = 140*F lillTIAL CLAD TDIP = 1600*F ~' ll: 10 f.O i i i i 100 200 300 110 0 500 600 Figure 6-7. Quench Correlation and Heat Transfer Coefficient Versus Data, Cosine Power FLECHT SEASET Run #32013 B-41

) 12 0 co 7 10 'g g ICIEED ~ ~ CORRELATION Addb PRESSURE = 40 PSI A PEAK POWER = 0.7 EW/FT g g y FLOODING RATE = 1 IN/SEC ^ INLET SURC00 LIM = 5'F 2 = @' INITl/L CLA0 TDdP = 1600*F - 0 0' 0 100 30 300 400 50 0 600 700 800 hench time (sec) C. 'f R00 lH i df . --- n00 u 7,, H00 10J l E l ELEVATION = 6 FT ~ 50 8 M GIMELATICE-i. ')- 3, j ba l 5 l l h PIE 3SIE = 5 PSIA }g I g Vj J-PEAK POEX = 0.7 XW/FT R000 LNG MTE = I IN/EC l T 10 IILET SJ8C00 LIM = 5'F E INITIAL GAD TBf =f 6004 0 0 100 30 300 400 500 600 700 800 900 1000 Time (sec.) Figure 6-8. Quench Correlation and Heat Transfer Coefficient Versus Data, Cosine Power FLECHT SEASET Run #35114 B-42 I

4.0 12,0 h O CORRELATION O CC%D 3,o o00 3 8.0 hoo"O 3 o o j[00 ~ d 2.0 N o g OATA o CD 4.0 O t i e f g g 30 400 600 Quenchtime(see) Z = 6.0 ft e I R00 ION I

ROD 76 80.0

[ ) 200 SF y p ... CORRELATION 2 9" P = 40 PSI A } W.0 9 max = 0.7 n/FT E AT,,= 140F Ti ni t = 1400F l 3.0 F Vlu = 4.M IN/3 FOR 5 SEC 0.42 IN/3 FOR REST r . ' GF Tile TIME a a 1 t a a f 230. 0 400.0 800.0 Time (sec) Figure 6-9. Quench Correlation and Heat Transfer Coefficient Versus Data, Cosine Power Fl.ECHT SEASET Run #32333 { B-43

l 1 57.s= E 2c l ss.s=_ 7 3 G 51.5=_ 43.s=_ ~. 4 g

3.r=_

t = E=g v.s= _ m

=

is. s=_ u. =_

. c !

i. u s.= ts.= d.= d.= a= d.= 1

s. =

timxia o I HEAT TRAN CORR Figure 6-10 a): Predicted Heat Transfer Coefficient l for Skewed Power Run ADKAATR B-44 f

~

15. =

Ehc ( 4.%, i= I2 - 2 X le L Z.CCC. I i to. = _ l [ 5.::=_ = o i l s.c=_ f i 4.CCC_

.3CC_

l I i ? c.=. t } O

.:::=

s.= ts.c:=

..=

32. =

.c. = ... = TIME (X1C 11 QUENCH HF_IC-HT Figure 6-10 b): Predicted Quench Elevation for Skewed Power Run ADKAATR f B-45 \\

67.sG3 Sha b 53.sm. t" t !.5 Ez 5.sa:_ l C A 35.sm_ acg R=5 27.s02_ ts.nac. L 1.sG2_ 3 Sm, l C. o.cco 7.000 t s.cas

21. 32 ts.=c

s.:m 42.:=

1 TIMECX10 11 { HEAT TRAN CORR Figure 6-11 a): Predicted Heat Transfer Coefficient for Skewed Power Run ADKADZD B-46 f

15 CIX: s i 9 2 t.. cts _ iE Ea 12.0a0 to.ctm. C s.m-5 s.cao_ a.oac_ z.ccm_ s.cac 6 i v o.cao 7.::co 14.::00 21 :0D 3 ::8 TIME!X10 11 QUENCH HEIGHT Figure 6-11 b): Predicted Quench Elevation for Skewed Power Run ADKADID B-47

7. FLECSET Computer Code Listing C * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * *

C C

PEFLOCD HE AT TR ANSFER COEFFICIENT CCRR EL ATION C C REF. ----- NUREG/CR-2256 NOVEMBER 1981 C C * * * * * * * * * * * * * * * * * * * * * * * * * * * * ' " ' ' ' ' ' ' " " ' * * * " " ' ' ' " ' C RE AL K F.KG.NU1.NU2. NU3.NU DI MENS ION Q AXZQ t1001.0 AXTe t1001.F AXTB t1001.F AX Z t100 ) 1 .P DC A Y t 10 01.PDCT t100 3. V INTM (10 0 3. VINT a ( 10 0) DIMENSION TX(2001.HTCl3001.ZDNCHt3001.AFRAYIl01 COMPON /STP /IUNIT. t FL A G.!P HASE.T.P.V.H.S.U.X CSUBP I, 1 XK AP P AI. BET A l. SPEED C CALL INLIST C C SET DEBUG FL AGS IDBUG = 0 ID BILG = 0 CC ' " " ' " ' " * * * * * * * * * * * * " ' ' " * * * ' ' " ' " ' ' ' ' " ' " ' ' ' ' C C GENEEAL INPUT C C ' " ' ', ' ' " ' ' ' ' ' ' ' ' * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * *

C READ 15 10 0 0 l DT SU S.F.TI NI T.P WF T.NR C ALL PIKL t SHD*SUBIFl.DTSUB.7HP t PSI Al.F 8HT!hlT t Fl.TINI T 1.11HP h F T I K W / F T 3.* W F Y. 2H M R. M R I 1000 FDP. MAT (4F10.5.155 READ (5 10103 Z.ZDBUG.ZPEAK.DR.0E.A CAL L P IKL t 5FZlF TI.Z 9HZDBUG t FT I.ZDBUG.9MZPE AK t FTI.Z PE AK 1.6HDR (FTI.DR.6HDE t FTI.DE.6HA IF T28. Al 1010 FORPAT I5F10.5 F 10.8 3 READl5.10155 POP 3X.RCPAF.RCPAR CALL FIKL(8HPOP0Xt-l. POP 0X.5HRCFAF.RCPAF.5HfCPAP.4CPARI 1019 FORPAT (3F10.8)

READ (5 1020) NVIN.NDECAY NINTPR.NPSHPE CALL P IKL (4HNVIN.NVIN.6HNDECAY.NDECAY 6HNINTPR.N! hTPR. 1 6HNPSHPE.NPSHPEl 102 0 FORMAT t41101 C C *************************************************** C C TABLE OF TIME VS VIN C C * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * " ' ' C WRITEt6.11001 110 8 FOR M AT (1HO.2X.* TABLE OF TIME VS VIN */3 WRITE 16.1105) 1105 FORPAT (10 X.

T I ME '.10 X.
V I N IIN /$ 1 * / 3 DO 1110 J s 1.NVIN READ (5 13003 v!NTN tJ).VINTB tJ1 1

WRITE (6.1301) VINTMtJi,VINTB(J) 1110 CONTINUE C ************************************************** C C T ABLE CF NCAM A LIZEC POWER CECAY C. l B-48 )

C We!TE (6 12301 1200 FORMAT (1HO. 2X.*T ABLE CF NORMALIZED POWER DECAY */1 WRITE (6.12103 1210 FORPAT ( 10 X.

T IM E *.10 X.
PDCAV */3 00 1220 J = 1.NDEC A Y READ (5.13033 PDCTtJI.PDCAYtJI WRITE (6 1301) POCitJI.PDCAYtJ) 122F CONTINUE C

C * * * * * * * * * * * * * ' ' " ' ' " * * * " ' ' ' ' ' " ' ' ' ' ' ' ' ' ' ' " ' " ' ' ' ' C C TABLE CF NORMALIZE 0 INTEGRAL OF POWER C C

- - ''"""""''''''"""*4'"

C WRITE (6.12301 123 0 FORPAT (1HO.2X

NOANALIZED INTEGR AL CF PCWER */1 WRITE (6 1248) 1240 FORPAT (10X.'HEIGHTIFil'.5X.' QAXTBS '/3 00 1250 J = 1.NINTPR READ (5 13001 QAXZQtJ).QAXT8tJI WRITE E6.13018 G4XZCtJl.0AXTBtJ) 1250 CONTINUE CC * * * * * * * * * * * * * * * ' ' ' ' " ' ' ' " ' " ' " ' ' ' " " ' ' " ' " ' ' ' ' ' ' "

C C TABLE OF ARIAL POWER SHAPE FACTOR C C * * * * * * * * * * * * ' ' ' " ' ' ' ' ' ' ' ' " ' ' ' ' ' ' ' ' ' ' ' ' " ' ' ' " " ' ' ' ' ' ' ' C WRITE (6.12608 1260 FORPAT tiH0 2X.* TAeLE OF AXI AL POWEF SHAPE FACT 02 '/l WRITE (6.12701 127 0 FOR PAT t 10X.' FAX 7tFil '.5X.* F AXTa */l DO 1280 J = 1.NPSHPE READ (5 13301 FAXZlJ).FAXTBtJI WRITE 86.1301) F AX Z lJI.F AX TB tJ 1 128 0 CONTINUE CC * * * * * * * * * * * * * * * * * ' " ' ' ' ' ' " ' ' " ' ' " ' ' " ' ' ' ' ' ' ' ' " ' " ' ' ' ' C C INPUT IS CCMPLETE C C

- - - - r******

1300 FORPAT(2F10.53 1301 FORP AT (10X.2F10.51 C C * * * * * ' * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * *

C STEAP PROPEE TIES USING STP C

C * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * ' ' ' ' C C BRITISH UNIT IUNIT = 2 IFLAG = 1 ) PS AVE = P j C LIQUID SAT PROPERTIES IPHASE = -1 CALL ZZP HF =H VOLF = V TSAT =T CPF = 1.0 /CSUSF1 B-49

I 3 U/$-FT*F LIQ TM. CON". gaf C = TCW i! UNIT. I CHEK.V.T l /3 6C 3. 0 e C SAT LIQ VISCOS ITY L9h/FT-SEC VISF = DVW IIUN IT. ! CHE K.V.T I'3 2.0 C $4T W APCR PROP ERTI ES HG.SP.VOL IPHASE = 1 P = PSAVE CALL ZZP P = PSAVE HG=H VOLG = V C SAT THER. COND STU/S-FT-F KG = TCWIIUNIT.! CHEK.V.T l /360 0.0 W R ITE t6,2 0 0 lT S AT.V OLF.VOL G.HF.HG.KF.K G.v !S F.CP F 200 F OR M AT (1 HO. 2X.* TS AT = *. F 10.6. 5 X.

v0LF = '. F 10.6 5 X.
v0L G = '.

1 F 10.7.5 X. 'HF ='.F 10 5. 5X.

HG='.F 10.5.5 X. 'KF ='. F 10. 7 #

2 S X.'K G= *. F 10.8.5 X

V I SC = '. F 10. 7. 5 X. 'CP F = '. F 10. F l C

C PROPERTY CALCULATION IS OVER C C ***************************'" ''' " '" " "' C C CALCULATION BEGINS CC ' ' ' * * ' " ' ' ' ' ' ' ' " " ' ' ' ' ' " " ' " ' ' " " " " ' " ' " " " ' C WRITE t6.20508 2050 FORMAT (1H1 9X.20H"'***************./l WRITE (6.2060lZ 2060 FGRPAT (10 X.*THE R ESUL TS CF THIS TEST CAS E*.5X.*Z =

1 F10.5.5X.* FT '/l WRITE (6.2070) 2070 FORPAT tiOX.20H""'**********.//l WR I T E (6.P1001 210 0 FOR P AT (15X.4HTI ME.8 X 1HH.8X.6H ZQ tF T).8X.5HH t313.

1 7X,5HZQ tM ).3X 8H f Q t !N/$ 3. 4X.9HVI N t !N/Si l WRITEt6.21013 2101 FOR P AT (2 3X.14H tBT L/HR-FT2-Fl //l CALL I NT ER P t F AX Z.F A X T B.hPS HP E. Z.F A X ) QM AX = PWFT' POP 0X TINITZ = (T! NIT-TSAT)' FAX +T3AT Hi = 0 215 'QM AX'O.9 481*F A X/RCP AR

t i.-E XP t-( T IN I TZ-7 00. 3 /435. ll IF ITINITZ.LT. 700.3 H1= 0.

R H O G= 1./ VO L G aHOF=1./v0LF RHO GF= RHOG /R HCF CTsITINIT-TSATl/ISGO.-TSATI HFG=HG-HF H H1 l H$1=H'5.67826 DZQ = 0 005 T=0. 20=0. CALL INTER P tQ AXZQ.0 AXTB.NINTPR.ZPE AK.0AX ZPK) CALL I NTER P t v !NTM.V I NT8.NV I N.O..V I N I JTYPE=0 IPLOT = 1 I=1 Jag 15 CONTINUE C * * * * * * * * * * * * * * * * * * * * * * * * ' * * * * * * * * * * * * * * * * * * * * * * * * * * *

I C

C COM*UTE QUENCH FRONT ELEVATION C B-50

C ******" '" " '" '" " " '" " '"'"' C IF (ZO.GE. ZDSUG) 108UG = 1 IF (ZDBUG.LE. D1 108UG = 0 IF IIDOFLG.NE. Of IDBUG =0 20 Z0+0Z0 DD 40 IVQ=1.2 IF (IVO.EO. in 20=Z0.0005 IF tlVQ.EQ. 23 ZQ=20+.0005 CALL INTERP (QAXZQ.0AKT8.NINTPR.ZQ.QAXl QEQ1 = QMAX IFtMR.EO. 280EQ1 = QEQ1'1.1 GEQ = QEQi CALL I NTER P t F AXZ.F A XTB.NPS HPE. ZQ.F AX) TINITE=tTINIT-TSATl* FAX +TSAT DTC=800. DTE=DTG/ti.+60.ti.08'tTINIT-TSATl/DTC-1.2611 TE=TINIT+DTE TE ZsTS AT+ tTE-TS AT I'F AX QEFFZm.7' FAX'.9491 CALL I NT ER P l V INTM. V I NT 8.N V I N.T. V! hl RE = VI N/12.'R HOF 'DE/ VI SF FH= 1. / ti.+ 7 0. ** ti..0133' t 2P E A X/CR i l l ZS = 6329.* t R E +40 00. I t-1 46 8 8 ' VIN /12.'RH3 F 1*CPF'DE*DE/KF'FH Z40=0. 85 2' R CP AF 'DT S UE*V IN/12./ QM AX/. 9481.2 34' P CP AR 1* t T INI T-TS AT I' VIN /12./cP A X /.94 81+1.167'F H IF tZ AD.L E. 0.1 ZAD=0. FDTSU8sEXP t-10.09' t CPF 'DTSUB/HF Gil F v l N2:1. 3* F X P I-1. 65 2E-9'R E

R E/ R HC GF . 5 24 9 F V i h3= EXP t - 7.29 3E-9'RE *RE / RH3G F.524 8 FW I h4= 6620 3. 'RNOGF * *.2682/RE" i.1-2 8' EX P t. 00 012 2' 1R E /F NO GF ". 262 )

FWIN5=1.+.5/ti.+50**t2..00038137'eE/RHOGF**.262tl F Pi=1. +. 5'EX P t-5 6 251E +0 9' R HOG F'R HOGF

R POGF )

F P 2=17.3*EX P t-5.6 251E *0 8'R HOGF *P HOGF'R HOGF I FP3=FP1 F P 4=1. +. 32 / (1.+ 53. '

t 5.-25 2 0.* R HOGF i l CT=(TINITE-TSATl/t500.-TSATI t

FT1=1.01552+.01396'CT l FT2=1 05' EXPT.66.59'CTl F W S UB=.3 +. 7' t i. -E X P t -10. 31 E-8'R E

R E/ P HOGr * *. 52 6 i

ill-2.9E-11* RE*RE* R E /R HOGF * *. 78 6* E X P t -9 3 E-8 'RE*R E 2/R HOGF ".5 2 41/ t i.+5 0.*

t-15. 75 ' tCP F'DTSUS /HF Gl + 1. 333 t l IF (IDBUG.NE. il GO TC 400 CALL PI EL (1HT.T.2H ZO.ZQ. 3HF AX.F AX,2HRE.R E.2HFH.F H.2H ZS.ZS.

1 3 HZ A D. ZA D.6 HF DTSUS.F DTSUB.5H F WI N2.F V IN2.5HF V Ih 3.F V ! N3. 2 SHFWIN4. FV!N4.5HFVINS.FW INS,3HF P1.FP1 3HF P2, F P2 3FFP4.F P4. 3 2 HCT.CT. 3H F T 1.F T 1.3 HF T 2.FT 2. 5HF V SU B. F V S UB ) 400 CONTINUE 00 20 K = 1.3 CDL $=.9 4 81 *Q A X ZP K/ R HO F / A / W I N' 12. /HF G CQuGEQ'QDLS FVQ1=.7*ti.-EXPT .0 0008 01* RE/ RHOGF. 262 t l FV Q 2=6.45 8E-5'R E **1 9 38/R HOGF* *.50 7 8' t CC'DG /ZP E A x li.5 FVQ sFV0i +F VQ 2 FQ=1..16/ t i.+ 7 0.*' t 1250.' tDR / ZPE AKi-5 45 3 ) i 1/ti.+80.**t7 14'CQ-4.931) TQs (F DT SUB'F VQ* (F P i +F WIN 2 + F P2'F VI N 3) 1+FVIN4*FP38'tFT1-FT2'FYIN5*FP4)*FWSUB'FQ TO A = TQ TQ=ZPEAK/v!N'.00228'RE*RHOGF" t.262)*TQ TOPEAK = TO FR13.5 B-51

FR2s9 OR = QAX/QAXZPK FQs08+Fai'QR' EXPT-FR2'QR*QR8 TQsTQ'FQ T Qs 70/ VIN

12. + t TQ-ZQ/V IN'12.3 / f t. +50.*
it-(TINITE-400.3/t40C.-75ATill CA L L I NTER P IPDCT.POCAY.NDECAT.TQ.POEC AY I QE Os 0E01'P D EC AY IF (IDBUG.NE.

il GO TO 450 CAL L P IKL t 3HQEQ.QEQ.4HQ0LS.00L S.4HFVQ1.FVQ1.4HFVQ 2. FVQ2.3a* VQ. 1 F V Q.2 HF Q. F Q.3HTQ A. TQ A,6HTQPE A K.T QP E AK.3HQ A X.Q A X. 2HF Q. F Q. 2 2HTQ.TQ.6H80EC AY.P OECAY.3HQEQ.QEQ) 450 CONTINUE 20 CONTINUE IF (IVQ.EQ. il Z013Z0 15 (IVQ.EQ. il 7013T0 IF (IVQ.EQ. 21 202 Z0 IF (IVQ.EO. 21 702=T0 40 CONTINUE yQs(ZQ2-ZQ11/tTQ2-TQ11 VQ 1 NC H s V Q' 12. C C * * * * * * * * * * * * * " ' ' ' ' " ' " ' * * * * * * * * * * * ' " ' ' ' * * * * * * * *

C C COMPUTE HEAT TRANSFER COEFFICIENT C

C " '" " "'"" ''''''' " " C ZQM=ZQ'.3046 IF (J.EQ.11 WRITE (6.2200lT.H.ZO.H51.ZQM.VQlNCH. VIN C STOPE INIT !al V ALUES FDP PLOT IF (J.NE. il GO TO 300 TXtlPLOTI = T HTCt!PLOTI = H ZQNCHt! PLOT) = ZQ 300 CONTINUE T=T+020/VQ Xs4.'t20=ZADl/Z5 NU1=H1/360 0.*D E/K G H3 = 0E F FZ/I T EZ-T SA Tl /0R'1.21* t i.-E XP t. 0 0 0 0 305'P E/ EHOGF 1**.26218 2*t.714+.266* ti.-EXP t-3.0 5E-4'R HOGF ** 1 524/RE/R El l i NU 3s H3'0 E/ KG NU2 NU 3+ 10 8.'EXP t.0 00018 3' AE/ R HOGF.2 f 21' 1 EXPT.0534*tZ-ZQl/ DEI IF (ZQ.LE. ZAO) NUsNU1 IF (ZO.LT. (Z5+ZA0).ANC. ZG.GT. ZADI NUsNut' t it. -EX P t 2. 5' X-10. l l + t NU2-NUi' ( 1. -E XP t 2.5 'X-10. l l i 2* t i.-EXP t-XI .9'X 'E XP t-X'Xil IF (ZQ.GE. (Z5+ZA0ll NUsNU2 IF (Z.LE. ZPEAKI GO TO 27 CAL L INTERP IF AXZ.F AXTB.NPSHPE. Z.F AXl 27 CONTINUE IF (Z.GT. ZPEAKI NUsNU-44.2*ti.-FAXi' EXPT.00304 1*tZ-ZPEAKl/ DEI JT T P E sJT YP E+ 1 Hs N U' K G' 36 0 0. /D E H51=H'5.67826 IF(IDBUG.NE. il GO TO 500 CA LL P IKL t 1HX. X,3HNU1.NU1 2HH3.H3. 3HNU 3.NU3.3HNU2.NU2. 2HNU, NU, i 1HH.HI 500 CONTINUE IF (JT YPE.EQ.20l WA IT E 16 2200lT.H.ZQ,H51. ZQ4.VQ1NCH. VIN 2200 F O R P A f t 12X. F 10. 5. F 12. 4.F 10 5.F 12. 4. 3 F 10. 5 /1 B-52

IF (JTYPE.EQ. 20) JTYPE=0 Jad*1 C STORE INFORM ATION FOR PLOT IF(!. NE. 10) CD TO 310 TX(IPLOTI = T HTCt! PLOT) s H IF t h.GE. E0.0 3 HTCt!PLCTI = 60.0 I ZONCHtIPLOTl = 20 IPLOT = IPLOT+1 Ia 0 310 CONTINUE Ist+1 IFt20.GE. 12.1 GO TO 30 IF(108UG.EO. il 10 EFLG = 1 GO TO 15 30 CONTINUE C C * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * * ' ' " ' ' * * * * * * * * *

t C

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? 8. REFERENCES l l 1. N. Lee, S. Wong, H. C. Yeh and L. E. Hochreiter, "PWR FLE CHT SEASET Unblocked Bundle, Forced and Gravity Reflood Ta' k Data Evaluation and Analysis Report" s NUREG/CR-2256 (EPRI NI-2013 or WCAP-9891) November,1981. 2. RF' LOD 3 - Model for Multinode Core Reflooding Analysis, BAW-10148, Babcock $ Wilcox, Lynchburg, Virginia, May 1981 (initial issus). 3. UPIFLOD - Model for. Upper Plenum and Cold Leg Injection Reflooding Analysis, BAW-1724, Babcock & Wilcox, Lynchburg, Virginia, June 1982 (original issue). 4. Letter Memo from C. K. Nithianandan to Dr. Y. C. Yeh, Westinghouse Electric Corporation, " correction to NUREG/CR-2256," March 12,1982. S. Yeh, H. C., et al.."Reflood Heat Transfer Correlation," Nucl. Tech. 46, 473 (19 6. Lilly, G. P., et al., "PWR FLECHT Cosine Low Flooding Rate Test Series Evaluation Report," WCAP-8838, Ma e 1977. 7. Lilly, G. P., et al., "PWR FLECHT Skewed Profile Low Flooding Rate Test Series Evaluation Report," WCAP-9183, November 1977. 8. Cadek, F. F., et al., "PWR FLECHT Final Report Supplement," WCAP-7931 October 1972. 9. F. Aguilar et al., "STP - FORTRAN Librart Routines for Steam Table Properties," NPGD-TM-514, Babcock & Wilcox, Lynchburg, Virginia, January 1983, Rev. A.

10. McConnell, J. W., "Effect of Gecmetry and Other Parameters on Bottes Flooding Heat Transfer Associated With Nuclear Fuel Bundle Simulators," ANCR-1049, Aerojet Nuclear Company,1972.

1 (

11. Crapo, H.

S., et al., " Experimental Data Report for Semiscale Mod-1 Tests S-03-A, S-03-9, S-03-C, and 5-03-0 (Reflood Heat Transfer Tests)," ANCR-NUREG-1307, Aerojet Nucleae Company, 1976. B-54 _ _ - _ _ _ _ _ _ _ _ _ _ _ _ _ _ _ _}}

v t e Letter Sequence Other
TAC:53509, (Open)
Initiation Acceptance... Administration Questions Answers Results Approval... Other: ML20080L848
MONTHYEAR1983-09-30 [Table View]

ML20080L848

Text

SUMMARY

RESPONSE

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