ML20217Q929

Non-proprietay Version of Rev 2 to WCAP-14310, AP600 Design Certification Program SPES-2 Tests Final Data Rept

ML20217Q929
Person / Time
Site:	05200003
Issue date:	05/31/1997
From:	Conway L, Hundal R, Lofus M WESTINGHOUSE ELECTRIC COMPANY, DIV OF CBS CORP.
To:
Shared Package
ML19317C690	List: ML20217Q927 ML20217Q929 NSD-NRC-97-5209, Forwards non-proprietary Version of Rev 2 to WCAP-14310 & Proprietary Version of Rev 2 to WCAP-14309, AP600 Design Certification Program SPES-2 Tests Final Data Rept. Proprietary Version Withheld
References
WCAP-14310, WCAP-14310-R02, WCAP-14310-R2, NUDOCS 9709040008
Download: ML20217Q929 (38)

Text

Westmonoest N<w Paormaticy Class 3 =

-WCAP-14310 Revision 2 AP600 DESIGN CERTIFICATION PROGRAM SPES-2 TESTS FINAL DATA REPORT l-L. Conway

' R. Hundal M. Loftus V. Merrit M. Ogrinsh May 1997 WESTINGHOUSE ELECTRIC CORPORATION Energy Systems Business Unit P.O. Box 355 Pittsburgh, Pennsylvania 15230-0355 C1997 Westinghouse Electric Corporation All Rights Reserved 9709040008 970826 c:u632wvnumm. PDR ADOCK 052 3

- 2.6 Facility Operation The day before the test, SPES 2 personnel verify that:

e the plant is configured for the test e

all plant alarms and protection functions are operating a

the DAS test procedure can perform the required trips for the test

. - - all the control systems and auxiliary systems are operating e# the plant is ready for start-up .

On the day of the test, several key steps are performed to bring the plant up to initial conditions.

l The pressurizer intemal heaters are tumed on and the ADS-1 valve is opened until the primary system fluid temperature reaches 100*C, after which the level and pressure controls are set to auto mode.

When primary pressure is about 3 bar, the RCPs are started up. After the rod-bundle electric resistance check (it should be ~1.9 mO), the 4 MW power group is turned on to give approximately 60 percent of the maximum current (equivalent to -900 kW of generated power). The heat up and pressurization of the facility is carried out maintaining this power until the hot leg temperature reaches 200*C, while subcooling conditions in the circuits. Steam generator levels are brought close to the nominal value and the power channel power is increased step-by step using the 8 MW and 4 MW power groups. When nominal conditions are reached, they are maintained for about 500 seconds 1 O. before starting the transient.' To start the transient for all tests, a specific break valve (or valves if required) is opened to begin break flow. At this point, the transient follows a course of events that is specific to the test procedure for that particular matrix test.

However, some generalities of the sequence of events for facility operation can be made for most of -

the tests. Once a setpoint is reached initiating the R signal, the main steam line isolation valves are closed and the power decay-simulation (discussed in Section 2.5.1) is begun. Upon S signal initiation, the CMT isolation valves and the PRHR isolation valves are opened, and the main feedwater (MFW)

. isolation valves are closed, all with a 2-second delay. 16.2 seconds after S signal, the RCP coastdown is initiated. ADS-1 is actuated on CMT volume of 67 percent with the other ADS stages following the delay time specified in the test procedure. Heat loss compensation is terminated with ADS stage 1 actuation. The accumulators begin injecting when the primary system pressure falls to ~700 psia. The IRWST begins injecting water when the primary system pressure is 26 psia. The test is terminated when final conditions are achieved as specified in the test procedure. The specific facility operation and configuration for each test is discussed in subsections 2.6.1 through 2.6.13.

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2.6.1 Facility Operation for Test S00303 The purpose of test S00303 was to investigate the plant behavior and system response during a simulated 2 in, cold-leg break on loop B (the CMT side of the plant) with intervention of the passive safety systems only. The test was performed with the pressurizer to ChtT-A/ B balance lines closed by means of blind flanges installed on both the pressurizer and ChtT connections. The break was located at the bottom of loop B cold leg B2 between the cold leg B2 to ChfT B balance line and the power channel. De break line for the facility was configured as shown in Figure 2.6-1 with a break orifice installed as described in Figure 2.6.1-2. ne orifices installed throughout the facility are listed in Table 2.6.1-1.

Once the facility was at initial conditions, the test was initiated by opening the break valve. When the reactor trip R occurred (pressurizer pressure P 027P = 12.41 MPa = 1800 psia), the heater rod bundle power was controlled to match the scaled AP600 decay heat, and the steam generator MSLIVs were closed with a 2-second delay. When the S signal occurred (pressurizer pressure P-027P = 11.72 MPa

= 1700 psia), the PRilR isolation valves and the CMT injection valves were opened and the MFWivs were closed, all with a 2-second delay, and the RCP coastdown was initiated with a 16.2-second delay.

The CVCS, NRHR, and SFW were off throughout the whole transient. The test simulated the failure of one of two 4th-stage ADS valves on loop B. The ADS valves were programmed to open versus either CMT level L-A40E or L-B40E with the delay time shown in Table 2.6.12. The accumulators f were set to inject water via DVI when the primary pressure was lower than 4.9 MPa (710.6 psia). The I IRWST was set to inject water via DVI when the primary pressure was lower than 0.18 MPa (26.1 psia). The test was terminated when the flow rates (F-A60E/F-B60E) discharged by the IRWST reached a stable flow (without significant fluctuation).

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2.6.4 Facility Operation for Test S00605 m

he purpose of test S00605 was to investigate the asymmetric Ch1T performance with operation of the PRHR in conjunction with a simulated 2 in. DVI-B break (the CMT side of the plant) and passive i safety systems only for mitigation. The break is located on DVI B between the ECCS injection and the power channel. De test was performed with the pressurizer to CMT A/B balance lines closed by means of blind flanges installed on both the pressurizer and CMT connections. The break line for the facility was configured as shown in Figure 2.6.41 with a break orifice installed as described in Figure 2.6.4 2. The other orifices installed throughout the facility are listed in Table 2.6.4-1.

1 Once the facility was at initial conditions, the test was initiated by opening the break valve. When the reactor trip R occurred (pressurizer pressure P-027P = 12.41 MP3 = 1800 psia), the heater rod bundle power was controlled to match the scaled AP600 decay heat, and the steam generator MSLIVs were closed with a 2-second delay. When the S signal occurred (pressurizer pressure P-027P = 11.72 MPa

= 1700 psia), the PRHR isolation valves and the CMT injection valves were opened and the MFWIVs were closed, all with a 2-second delay, and the RCP coastdown was initiated with a 16.2-second delay.

The CVCS, NRHR, and SFW were off throughout the whole transient. The test simulated the failure of I of 2 fourth stage ADS valves on loop B. The ADS valves were programmed to open versus either CMT level L-A40E or L-840E with the delay time shown in Table 2.6.4-2. The accumulators were set to inject water via DVI when the primary pressure was lower than 4.9 MPa (710.6 psia). The h

'd IRWST was set to inject water via DVI when the primary pressure was lower than 0.18 MPa (26.1 psia). The test was terminated when the flowrates (F-A60FJF-B60E) discharged by the IRWST reached a stable flow (without significant fluctuation).

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TABLE 2.6.41 SPES 2 LNSTALLED ORIFICES Location Diameter (mm) Thickness (mm)

ADS-1 4.37 12 ADS 2 9.35 12 ADS-3 9.35 12 ADS-4A 20.68 7 ADS-4B 14.62 7 CMT-A injection line 4.1 5.5 CMT-B injection line 5.7 5.5 CMT-A cold leg bal, line (2 orif.) 7.5 5.5 CMT-B cold leg bal. line (2 orif.) 7.5 5.5 Accumulator A injection line 4.86 7.3 Accumulator B injection line 4.86 7.3 DVI B break device 2.56 3.3 *

• Rounded entrance with 2.6 mm radius O

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O TABLE 2.6.61 SPES 2 INSTALLED ORIFICES Location Diameter (mm) Thickness (mm)

ADS 1 3.09 12 ADS-2 9.35 12 ADS-3 6.61 12 ADS-4A 20.68 7 ADS 4B 20.68 7 Ch1T A injection line 4.1 5.5 l

Ch1T-B injection line 5.7 5.5 Ch1T A cold leg bal. line (2 onf.) 7.5 5.5 Ch1T-B cold leg bal. line (2 orif.) removed -

Accumulator A injection line 4.86 7.3 Accumulator B injection line 4.86 7.3 l

CL-BL-B break device Ch1T side 8.95 "

O CL BL-B break cold leg side 8.71 9*

9*

• Rounded entrance with 9 mm radius (see Figures 2.6.6-2 and 2.6.6-3)

" The actual scaled break size of the 8-inch Sch.160 CL BL is 8.71 mm. However, since no significant amount of break flow is discharged from this point, the 8.95 mm orifice from matrix test No. 6 was utilized (see Figure 2.6.6-3).

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TABLE 2.6.6 2 PROGRAMMED OPENING OF ADS VALVES Orifice Dia. CMT Volume L A40E or L-B40E Delay Time ADS Stage (mm/'m.) (%) (m/ft.) (sec.)

First 3.09/0.122 67 4.152/13.622 30 Second 9.35/0.368 67 4.152/13.622 125 Third 6.61/0.260 67 4.152/13.622 245 Fourth A 20.68/0.814 20 1.192/3.911 60 see after 20% CMT vol.,

but no sooner than 360 sec.

after 67% CMT vol.

Fourth B 20.68/0.814 20 1.192/3.911 60 see after 20% CMT vol.,

but no sooner than 360 sec.

after 67% CMT vol.

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TABLE 2.6.91 SPES 2 INSTALLED ORIFICES location Diameter (mm) Thickness (mm)

ADS-1 4.37 12 ADS-2 9.35 12 ADS-3 9.35 12 ADS 4A 20.68 7 ADS-4B 14.62 7 CMT-A injection line 4.1 . 5.5 CMT-B injection line 5.7 5.5 l CMT-A CL bal. line (2 orif.) 7.5 5.5 CMT B CL bal line (2 orif.) 7.5 5.5 Accumulator-A injection line 4.86 7.3 l Accumulator B injection line 4.86 7.3 SG B tube break device 0.85 5*

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• Rounded entrance with 0.9 mm radius O

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TABLE 2.6.9 2 PROGRAMMED OPENING OF ADS VALVES Orifice Dia. CMT Volume L A40E or L B40E Delay Time ADS Stage (mn/m.) (%) (m/ft.) (sec.)

First 4.37/0.172 - .

2 min + 30 see after "S" Second 9.35/0.368 - -

2 min + 125 see after "S" Third 9.35/0.368 - .

2 min + 245 sec after S" Fourth A 20.68/0.814 20 1,192/3.911 0 see after 20% CMT vol..

but no sooner than 360 see after 67%

Fourth B 14.62/0.576 20 1.192/3.911 60 sec after 20% CMT vol.,

but no sooner than 360 see after 67%

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TABLE 2.6.101

\ SPES 2 INSTALLED ORIFICES Location Diameter (mm) Thickness (mm)

ADSl 2.2 12 ADS-2 9.35 12 ADS 3 2.2 12 ADS-4A 20.68 7 ADS-4B 14.62 7 l CMT A injection line 4.1 5.5 CMT B injection line 5.7 5.5 CMT-A cold leg bal. line (2 orif.) 7.5 5.5 I

CMT B cold leg bal. line (2 orif.) 7.5 5.5 Accumulator A injection line 4.86 7.3 Accumulator B injection line 4.86 7.3 SG-B tube break device 0.85 5*

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• Rounded entrance with 0.9 mm radius O

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TABLE 2.6.10 2 PROGRAMMED OPENING OF ADS VALVES Orifice Dia. CMT Volume L A40E or L.B40E Delay Time j ADS Stage (mm/m' .) (%) (m/ft.) (sec.)

First 2.2/.0072 67 4.152/13.622 30 Second 9.35/0.368 67 4.152/13.622 125 Third 2.2/.0072 67 4.152/13.622 245 Fourth A 20.68/0.814 20 1.192/3.911 60 see after 20% CMT vol.,

but no sooner than 360 sec.

after 67% CMT vol.

Fourth B 14.62/0.576 20 1.192/3.911 60 see after 20% CMT vol.,

but no sooner than 360 see, after 67% CMT vol.

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2.6.11 Facility Operation for Test S01512 Test 501512, a large steam line break with passive safety systems only, was simulated using the steam generator.A PORV as tne break opening. The steam generator A PORY had an orifice installed with a diameter of 20.4 mm (shown in Figure 2.6.11 1) which corresponds to an AP600 break area of 2

1.388 ft . (This area corTesponds to the steam generator outlet nozzle orifice area.) The other orifices installed at the facility are listed in Table 2.6.11 1.

Test S01512 was performed with the facility operating at full pressure and flow, but at

• hot standby" conditions. The power channel was at zero power (i.e., no decay heat was simulated) but with heater rod power at 150 kW for facility heat loss compensation. Additionally, the following initial conditions existed:

RCPs were running at nominal flow (cold leg flow = 12.92 lb/sec.)

+

pressurizer pressure was at 2250 psia core AT was - l'F (Tavg -545'F)

• pressurizer level was between 6.56 ft. and 8.2 ft.

steam generators pressute was approximately 1000 psi steam generators narrow range level was approximately 4.9 ft.

main feedwater isolation valves were closed a

common steam line isolation valve (BV-07) was closed C

• main steam isolation valves (BV-05A/BV-05B) were opened

\

• CVCS, NRHR, and SFW were not oprational.

The test was initiated by opening the steam gen 3rator A PORV (BV 06A) at time zero. All heat loss compensation was terminated when the steam generator A PORV was opened. Based on pretest predictions using a lead / lag function of 50/5, the S signal was manually generated by the SPES plant computer one second after the break opening. De pressurizer internal heaters were shut off by the S signal. Also, at S signal, the Ch1T and PRHR isolation valves were opened with a two second delay, the main steam line isolation valves were closed with a 4-second delay, and the RCPs were shutdown with a 16.2-second delay.

The ADS was not expected to actuate for this test, but was programmed to open versus Ch1T level with the appropriate time delays as listed in Table 2.6.11-2. The accumulators were pressurized to inject when the primary pressure was reduced to less than 696 psia. The IRWST was at full normal level such that it would inject water when the primary pressure was lower than 26.1 psia. The test was terminated when the primary system temperatures and pressures had stabilized and the Ch1T level was not decreasing.

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TAllLE 2.6.11 1 SI'ES 2 INSTALLED ORIFICES Location Diameter (mm) Thickness (mm)

ADS 1 4.37 12 ADS 2 9.35 12 ADS-3 9.35 12 l

ADS-4A 20.6S 7 A954D 20.68 7 CMT A injection line 4.1 5.5 CMT B injectior line 5.7 5.5 CMT A CL bal. line (2 orif.) 7.5 5.5 CMT B CL bal. line (2 orif.) 7.5 5.5 Accumulator A injection line 4.86 7.3 Accumulator B injection line 4.86 7.3 Steamline-A break device 20.4 10 *

• Rounded entrance with 5 mm radius 9 O

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TABLE 4.1.2 2 SPES.2 HOT PRE. OPERATIONAL TEST H.01 FACILin' l

HEAT LOSSES VS. TEMPERATURE Channel Total Estimated Time l Hot.Les Power (38 Power (2) Heat 14ssesH3 Interval (l)

Temperature (kW) (kW) (kW) Source File (sec.)

l J l

l I

Notes:

(1) This time interval is considered valid for the value of dita recorded.

(2) The total power includes pump heat power released to fluid:

Pump A = [ )(a.b.c)

Pump B = [ ]<a.b.c)

O (3) Electric power input to power channel.

(4) The estimated power has been evaluated with a bestfit quadratic equation based on the measured data:

l HL = [ )(tb.c) where:

!!L = Heat losses (kW) l T = Hot leg temperature T.A03PL ('C) '

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TABLE 4.1.2-3 0 SPES-2 IIOT PRE-OPERATIONAL TEST 11-01 MAJOR COMPONENT IIEAT LOSSES

't 3 How rate in each cold leg = 0.619 kg/sec.

k Total power = 142.6 kW b

g Component liest Ims 7 Metal Mass Component flest Intet Average Temperature Outlet Average flest lesses Percentage due to Component lim /" Capty. (Btuf*F) CF) Temperature CC) (kW) the Cerripanent (%)

i g PC/IIL

$ l (A&B)

RCP.A/

l Cl AI.A2 s RCP-H/

h l CL-Bl,H2 U SG-A SG-H _

Total liest Losses = [ ] 'O*'

Notes:

(1) The weight of these components skxs not include flange and imiting metal masses.

(2) These data are not relevant for the calculation of steam generator hest losses, as their metal heat capacity ctmenbutkm can be negleticst (3) Pump power released to the fluid at low flow can be neglected.

(4)"Ihe difference between total power and total heat losses is due to the heat capacity of the system.

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TAIll.E 4.1.2 4 SPES2 PRE OPERATIONAL TEST !! 01 FACILITY SYSTEM HEAT CAPACITIES Time Calculated Calculatal Temperature Total Power Source File Inten al(3) Heat Heat Linear input Rate (2)

(sec.) Increase ('C) (kW)

.)

acqdat.spes.dat;242 acqdat.spes.dat:242 acqdat spes.dat:244 Average Heat Capacity = 8480 Notes:

(1) This time interval is considered valid for the value of data recorded.

(2) The total power includes pump heat power released to fluid:

~~

Pump A = kW Pump D = kW O

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TAllLE 4.1.2 5 SPES 2 IlOT PRE OPERATIONAL TEST 1105 INITIAL CONDITIONS Condition Specified Aetual

- < nn.-s Pressurizer pressure 3o0.5 psig (24.9 bar)

Pressurizer level 12.4 ft. (3.78 m) 110t leg temperature 415.6'F (213.l'C)

Cold-leg temperature --.

Power (kW) 192.3 Upper-head flow rate 0.40 lb/sec. (0.18 kg/sec.)

Steam generator pressure 270.6 psig (18.66 bar)

Steam generator level >36.2 ft. (>l1.02 m)

Accumulator pressure 197 psig (13.59 bar)

Accumulator level 6.86 ft. (2.09 m)

IRWST level 28 ft. (8.53 m)

Cold-leg /CMT balance line Cold-leg temperature temperature CMT external vessel not pressurized PRilR supply line temperature 302'F (150'C)

Pressurizer Cold-leg balance line >437.9'F (>225.5'C)

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drained at this time (data plots 20 through 23) and did not affect the rest of the test. De accumulator injection was initiated when the primary system pressure dropped below [ )(a.b.c) psia prior to ADS 1 actuation. Ilowever, the injection rate was low (less than [ ](a.b.c) lbm/sec.) due to the small difference between the primary system and accumulator pressures (data plot 39).

l Facility Response During the PDP:

De s,, stem response during the PDP was almost identical to that of test S00303, with the exception that ADS-1 occurred [ ](a.b.c) seconds later in this test S00504 The oscillating now that was observed in the tubular downcomer and in the rod bundle following the RCP coastdown continued into the PDP. The Dow oscillations resulted in large oscillations of the steam fraction of the two phase mixture exiting the rod bundle and flowing into the hot legs (data plots 30 and 31). Dese oscillations in steam fraction had a significant effect on the thennal buoyancy head that drove the now through the primary system at this time. The Guid steam fraction oscillations were observed through the hot leg and the steam generators (data plots 20 and j

21). However, the two-phase mixture entering the steam generators left the steam generators as saturated water (data plots 24 through 27). Some of the steam was condensed in the U tubes (the primary-side pressure was higher than the secondary side pressure at this time, allowing some heat to be transferred to the secondary-side fluid). De remaining steam was separated from the two-phase mixture in the high point of the U tubes due to the low velocity, which eventually caused

(]

V the U-tubes to begin to drain. For steam generator A, primary system How continued until 210 seconds into the transient, then intermittent flow was observed through steam generator A (plots 20 and 22). His was caused by the oscillations in the steam fraction where the buoyancy head in the hot leg was high enough to spill over the top of the U tubes at the peaks of the oscillating buoyancy head. At approximately [ )(n.b.c) seconds ([ )(a.b.c) seconds), all now through the steam generators ended since the free-water surface in the U-tubes had fallen too low to be overcome by the buoyancy head oscillations. These oscillations were seen in temperatures and pressures throughout the primary system. When the cold leg side of the steam generator U-tubes were completely drained (about [ ]<a.b.c) seconds), these oscillations stopped.

He primary system pressure decrease during the PDP began at a slow rate of ( )(a.b.c)p3if3,c, At approximately [ ](a.b.c) seconds into the event, the primary system pressure decay rate t

increased to [ J a.b.c) ps /sec. This happened when the Ch1Ts transitioned from their recirculation mode cf operation to their draindown mode. This transition ouurred when the B-loop cold legs partially drained and the Ch1T balance lines drained. This resulted in a higher Ch1T injection rate (Figure 4.2.41). The increased rate of pressure decay in the primary system was due to the increased injection rate of the cold liquid from the Ch1Ts (occurred at different times for the two Ch1Ts).

The Chits began injecting cold Guid into the annular downcomer [ ](n.b.c) seconds after the S signal occurred. Initially, this injection was by natural circulation at approximately 0.12 lbm/sec.

(] through each Ch1T, with hot fluid Dowing from the cold leg through the cold leg balance line V

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(CLBL) into the top of the Ch1T, and cold Guid flowing from the bottom of Chit. Between [

](a.b.c) seconds (data plot 38), Ch1T-A transitioned to draindown mode when cold leg D2 partially drained and subsequently the cold-leg balance line (CLBL) for Ch1T-A drained, and a free water surface developed in the top of the Ch1T A as the level started to drop (data plot 33).

The ChfT injection now, when draindown began, increased to approximately 0.28 lbm/sec. and gradually decreased as the Ch1T level decreased (reducing the driving head). See data plot 38.

For ChtT B the transition from recirculation to draindown occurred at approximately

[ )(a.b.c) seconds (earlier than for ChtT A), and its injection now increased to approximately

[ )(a.b.c) lbm/sec. and gradually decreased.

The free-liquid surfaces in the ChtTs were established by steam flowing from the cold legs to the Chits through the CLBLs. He steam flow from the cold legs condensed in the Chits and heated the free water surface. For Ch1T A, the Chit water surface was heated by the stream to saturation temperature (data plot 15) and flashing could occur as the pressure decreased in the system.

Both the recirculation and draindown modes of Chit operation established a stable thermal gradient in the Ch1T water The Chit water maintained a stable thermal stratification throughout its operation.

De accumulators began to inject fluid into annular downcomer via the DVI lines when system pressure dropped below [ )(*A*) psia (at approximately [ ](a,b.c) seconds). liowever, the injection rate was very low prior to ADS-1 (data plot 39).

Throughout the PDP, the PRiiR removed energy from the primary system. Ilowever, the combined effect of the PRilR cooling the prim:uy Guid and the cold injection flow from the i

CVCS and Ch1Ts was sufficient to limit the steam fraction of the two-phase fluid Dowing through the rod bundle and rod bundle cooling was maintained during this phase (data plots 30 and 31).

Automatic Depressurization System Phase ([ ](a,b,c) Seconds to End Of Test)

The automatic depressurization system (ADS) phe.se began with the actuation of ADS 1 and continued until the end of the transient (Figure 4.2.4-1).

Facility Response During the ADS Phase:

With the actuation of ADS-1, followed by ADS-2 and ADS 3 within approximately

[ ]ta.b.c) seconds, the rate of system depressurization increased from [ )(***) psi /sec. at the end of the PDP to [ )(*AC) psi /sec. at the start of the ADS phase. This rate gradually kereased as system pressure decreased.

O mia;WDJ63;wnon\wc-4'J632w.2a hon:Ib-o$(997 4,2,46

l steam from the two-phase mixture from the hot leg at the low How velocities existing at natural f

\

circulation flow conditions. De Guid level on the hot leg side of the U tubes oscillated as it decreased. His condition continued until approximately [ ]("A') seconds into the transient, at which time the top of the U tuber remained filled with saturated vapor and the U-tube water level decreased smoothly.

De fluid level on the cold-leg side of the steam generator A U tubes exhibited significant level oscillations from about [ ]("A') seconds and it appeared that intermittent now over the I top of the U tubes occurred. At [ ]("A*) seconds, the U tube water level decreased smoothly and was drained at about [ ](*AC) seconds.

Because of the higher steam fraction of the fluid in hot leg B and steam generator B, the time over which oscillations occurred was reduced and the U tubes filled with saturated vapor sooner. As a result, the steam generator B U tubes began to drain at about [ ]("A') seconds.

The level in the steam generator B hot leg side U tubes dropped to near zero at about

[ ](*A') seconds. The cold leg side U tubes exhibited significant level oscillations from about '

[

]("A') seconds which continued until the U tubes were drained ](n.b.c)atseconds

[ (data plots 22 and 23).

• Ilot Legs ilot legs-A and B were full of two-phase Guld until ADS 1 was actuated, when the measured level decreased (data plots 20 and 21). Le hot legs wen: nearly drained at ADS-4 ([ ](a,b.c) seconds) and partially refilled after IRWST injection began. De principal difference between hot legs-A and B was the innuence of the PRiiR llX on the void fraction in the hot legs during the PDP. Assuming that the fluid in the hot legs initially had the same steam fractions at the outlet of the power channel lower upper plenum, the PRiiR appeared to have preferentially removed steam from hot leg A (as seen in the very high steam fraction for the PRIIR inlet Dow)-thereby reducing the steam fraction of the fluid in hot leg A to less than the Guid steam fraction in hot leg B. The apparent steam fraction in hot leg A was [ ](a.b.c) percent at [ ]ta.b.c) seconds; while in hot leg B it was [ ](*A*) percent. The hot leg steam fraction affected the draining of the steam generators U tubes, with steam generator B draining earlier than steam generator-A.

• Cold Legs Cold legs-Al and -A2 remained full until [ ](ahc) seco. ds (data plots 22 through 27), at which time the level decreased to the horizontal section of the pipes and drained at about [ ](*AC) seconds. When ADS-4 occurred, the water level in the tubular downcomer temporarily dropped reaching [ ](**C) ft. below the hot-leg elevation at [ ](*A*) seconds (data plot 24). He rod bundle steam fraction fluid increased. After IRWST injection began at [ ]("A') seconds, the O annular downcomer re011ed and the cold and hot legs were partially refilled after [ ](**d seconds to the level of [ ](*A*) ft. above the hot leg.

mvuu632wnonssec-49632w.3.non itwoso997 4.2.5-11

Cold legs-B1 and B2 remained full until approximately [ )(*A') seconds into the event, at which time both cold legs B1 and D2 drained rapidly to the level of the horizontal section of the pipes. 'Ihis reduced water level in cold leg BI and cold leg B 2 initiated the transition of the CMTs from their recirculation to draindown mode of operation. Cold legs BI and D2 were refilled at [ )(*A') Seconds to the level of [ )(*A') f t. above the hot leg. At this time, the cold leg to CMT balance lines were partially filled.

• PRIIR and IRWST At the initiation of the test, the PRHR HX was filled with subcooled liquid. When the S signal occurred, the PRHR HX isolation valve opened and flow started through the HX at a high flow rate due to the still operating RCPs. When the RCPs were shutoff and the power channel upper plenum and the hot legs filled with two-phase Duld, a large portion of the steam in hot leg A Dowed to the PRilR HX (data plot 29). The two-phase mixture, consisting of altemating slugs of steam and water, was condensed and subcooled in the PRilR llX (data plot 28) from [ )(n.b.c).p to below [ ](*A*h .F During the PDP (prior to ADS 1), there was a significant variation in the flow through the PRilR HX, caused by the variation in the steam fraction in hot leg A. Steam condensation was apparently occurring in the PRiiR HX as evidenced by the rapid and wide variations in dP measurements (data plots 28,29, and 37).

When ADS 1 began, the power channel and the hot leg were refilled with subcooled water by accumulator injection. 'Ihe driving head for the now in the PRHR HX decreased (caused by the density difference between the Guid in the PRilR supply line and the retum line) and the now decreased and stopped. There was a short period of reverse flow at the end of the accumulator discharge. The subcooled Guid in the hot leg never filled the PRHR supply line, and hot fluid in this line flashed as system pressure decreased. Simultaneous Dashing in the supply line and condensation in the PRHR HX resulted in a wide variations in the measured flow in the PRHR HX retum line.

After the accumulator injection had ended, the rod bundle upper plenum again reached saturation temperature, and a two phase mixture again occurred in the hot legs. Flow restarted in the PRHR HX, and the now rate varied in response to the steam fraction in the hot leg. When ADS-4 fully depressurized the primary system and the IRWST Dow began and refilled the power channel and the hot leg with subcooled water again, the now through the PRHR HX stopped for the remainder of the transient. The subcooled Guid in the hot leg filled the PRHR supply line at [ )("A')

seconds.

Following ADS-4, primary system pressure decreased to near ambient, and gravity now due to the water elevation head in the IRWST began injecting water into the annular downcomer via the DVI lines. The flow from the IRWST was sufficient to refill the power channel, downcomer, and loop piping and to establish subcooled fluid now through the tube bundle and out through the ADS-4 flow paths (data plots 32 and 40).

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= Core htakeup Tanks ne Ch1T injection was initiated two seconds after the S signal when the Ch1T injection line I isolation valves were opened. Initially, the flow from the Ch1Ts occurred by natural circulation; hot water from cold legs flowed to the top of the Ch1Ts and cold water from the bottom of the Ch1Ts flowed to the downcomer, via the DVI lines, into the power channel.

Initially, this recirculation rate was approximately 0.13 lbm/sec. from each ChfT. The flow rate slowed down to ( ]<a.b.c) Ibm /sec. at [ )(a.b.c) seconds due to the decreased buoyant head driving force that occurred as the Ch1T water was replaced with hot water from the cold legs, and as the cold leg water temperature decreased.

After cold legs-B1 and B2 drained to the level of horizontal pipes at approximately [ )(a.b.c) seconds, flashing / draining began in the cold leg balance line. When the temperature at the top of the ChfT reached the saturation temperature for primary system pressure, a free water surface was established in the Ch!Ts. His increased the driving head for the injection flow and resuhed in a higher draindown flow rate. For the 1 inch LOCA, the break flow at this time was less than full ChtT draindown flow rute. His caused the Chit injection to consist intermittent short periods of draindown, which increased the cold-leg water level and short penods of refill with water from the cold legs. His resulted in a slow decicase in Ch1T levels and the ADS 1 actuation was therefom delayed and occuned at a system pressure of approximately [ ](*hC) psia, considerably below 711 psia accumulator gas pressure. Part of the accumulator coolant inventory was therefore injected into the primary system prior to ADS 1, his accumulator injection helped maintain the primary system coolant inventory at cold leg elevation and thus contributed to intennittent Ch1T draindown/ refill. For test S00401, the break was located in cold leg B2, resulting in cold leg B2 draining before cold leg-Bl. Since the Ch1T B balance line was connected to cold leg-B2, the draindown began earlier for Ch1T B (at 2170 to 2450 seconds) than for Chit A (at [ )(a.b.c) seconds), as shown in data plot 38. The ChtT balance lines finally completely drained at [ ](a.b.c) seconds (ADS 1), resulting in an increase in ChtT injection flow rate. De steam in the ChtT balance lines and at top of the Ch!Ts was slightly superheated as the primary system pressure was rapidly reduced by ADS operation.

He Ch1Ts were heated first by the hot liquid which replaced the cold water draining from the bottom of the Chits A stable, stratified thermal gradient was established in the Ch1Ts (data plots 15 and 16). Later steam from the cold legs maintained the exposed metal and free-water surface temperatures at or near saturation temperature.

The Ch1T recirculation mode flow rate was initially approximately [ ](*A') Ibm /sec. and steadily decreased to approximately [ )(*AC) lbm/sec. when the transition to draindown began, ne Ch1T average injection flow rate increased to approximately [ )(*AC) Ibm /sec during the transition period. After ADS 1 actuated, ChfT injection increased again to [ ](a.b.c)

Ibm /sec. and then gradually decreased with time. During the accumulator injection (ADS-1), the OV ChfTs'draindown rate remained high. Ch1T A was drained at about ADS-4 ([ )(a.b.c) mwuo0632wnonwe-40632w.3 non ib-osow? 4.2.5-13 Revision: 2

l seconds), ne CMT B injection flow rate decreased when the IRWST started at about [ ](n.b.c) seconds, and CMT B drained at [ )<n.b.c) seconds (data plot 33).

• Accumulators The accumulators provided water injection by a polytropic expansion of a compressed air volume stored within the accumulator. Accumulator injection started when the primary system pressure I dropped below 711 psia at [ ](a.b.c) seconds. He accumulator injection flow rate was low t

until ADS 1 was actuated at approximately [ J a.b.c) seconds when the flow rate increased to approximately [ ](a.b.c) lbm/sec. De accumulator injection after ADS actuation lasted approximately [ )(a.b.c) seconds, and the accumulators were completely drained (data plot 34).

The effective polytropic coefficient of expansion was calculated for the accumulators (Figures 4.2.5 3 and 4.2.5-4) to be [ )(a.b.c) for accumulator-A and [ )(a.b.c) for accumulator B. This was near the mid point between isothermal expansion (k = 1) and adiabatic expansion (k = 1.4) and showed that some heat was picked up by the compressed air from the internal metal surfaces of the accumulator during the expansion.

Mass Discharge and Mass Balance ne catch tank weight measurements are shown in data plot 43 for the break flow, for the ADS 1, 2, and 3 flows, and for the ADS 4 flow. The break flow as shown in plot 44, which began when the test was initiated, decreases as system pressure drops during the IDP and the PDP. When the ADS was actuated, the break location voided, and further discharge from the break was primarily saturated steam until IRWST injection refilled the cold leg after ADS-4.

The discharge from ADS-1, -2, and 3 was stable throughout the accumulator injection and increased temporarily when the injection ended. When ADS-4 occurred, the discharge of fluid from the top of the pressurizer essentially ended, and the fluid discharge from ADS 4 began. The ADS-4 fluid discharge rate was relatively stable and continued until the end of the test. De discharged masses are shown in Table 4.2.5-4.

De mass balance results for test S00401 were calculated based on water inventory before and after the test. Table 4.2.5-2 gives a detailed listing of the inventories of water in the various components before the test. Table 4.2.5 3 lists the inventories after the test and the amount of water injected into the vessel from the IRWST. The water level in the vessel was determined by the DP B16P measurement to be [ ](n.b.c) n. [ )(a.b.c) above the hot leg centerline at the end of the test. Table 4.2.5-4 compares the mass balance for the system before and after the test and shows 98.5%

agreement of the measurements, 9

m WW)o0632.wnwec.4o632. 3 non itsosow? 4.2.5 14

- _ ~

i 4 2.6 One.In, Cold Leg Break with Three PRHR HX Tubes, without Nonsafety Systems (501613)

( His matrix test was performed to be identical to matrix test S00401 with the exception that the number of PRHR llX tubes in use was increased from I tube to 3 tubes. His test simulated a 1 in, j break in the bottom of cold leg B2. He test began with the initiation of the break in cold leg-B2, which was the cold leg with the Ch1T B pressure balance line connection. The break location was just downstream from the cold leg to the core makeup tank (ChfT) balance line connection. His test was performed without any nonsafety systems (chemical and volume control system (CVCS) makeup pumps, steam generator stanup feedwater [SFW) pumps, and normal residual heat removal system '

[NRHR) pumps) operating.

Results are provided in the data plot package at the end of this section. The sequence of events for 501613 is listed in Table 4.2.61.

The AP600 SPES 2 tests were marked by distinctly different phases. These phases were characterized by the rate at which the primary system pressure decreased and the thermal hydraulic phenomena occurring within the primary and safety systems. The different phases selected for the purpose of detailed evaluation of this LOCA are shown in Figure 4.2.61 and are as follows:

• Initial depressurization phase (IDP)-Point I to 2 Pressure decay phase (PDP)-Point 2 to 3 O +

+

Automatic depressurization system (ADS) phase-Point 3 to 4 Post automatic depressurization system (post ADS) phase-Point 4 to 5 Overall Test Observations Figure 4.2.6-1 shows the plant primary system pressure during test S01613 (as measured at the top of the pressurizer), with selected component actuations and plant responses shown in relation to primary system pressure.

The IDP began with the initiation of the break, which resulted in a rapid reduction in pressure. The reactor trip (R) signal initiated at 1800 psia. The safety systems actuation (S) signal initiated at 1700 psia. The R and the S signals initiated the following actions:

Decay power simulation (with heat loss compensation) initiated hiain steamline isolation valves (htSLIVs) closed o'

hiain feedwater isolation valses (h!FWIVs) closed

• Ch1T injection line isolation valves opened Passive residual heat removal (PRHR) retum line isolation valve opened

+

Reactor coolant pumps (RCPs) stopped mnning

. Recirculation flow through the Ch1Ts and flow through the PRHR heat exchanger (HX) began immediately after their isolation valves opened. Flashing / boiling occurred in the rod bundle and mw600x32wnonsec.ex32w-wit 450997 4.2.6 1

upper plenum regions of the power cha mel due to the rapid decrease in primary pressure to the fluid saturation pressure. De measured fluid level in the upper-upper plenum decreased to the hot-leg elevation. The flashing on the hot leg side of the primary system stopped the rapid drop in primary system pressure. When the RCPs were shut off (at [ ](*AC) seconds), the flow through the rod bundle began to oscillate (with a [ ](*A')-second period). This resulted in oscillations in the rod bundle and lower upper plenum collapsed liquid level and fluid temperature, and system pressure.

During the initial stages of the PDP, the rod bundle collapsed liquid level decreased (fluid steam fraction inemased). His caused an increasing steam fraction in the upper plenum and the hot legs.

He hot leg-B fluid had a steam fraction close to that observed in the upper plenum. The steam fraction in hot leg A was lower due to the selective removal of vapor frorn the hot leg into the PRiiR liX inlet line.

Two phase flow in the hot legs initiated draining of the steam generator U tubes, as steam from the two-phase mixture collected in the top of the U-tubes. This stopped the primary system flow through the steam generatnrs so that the power channel flow was composed predominantly of the flow through the PRilR llX. The steam fraction oscillations observed in the rod bundle and in the upper plenum ended when the steam generator U-tubes drained. Approximately [ ](*A') seconds into the test, the steam generator B U-tubes began to drain. He steam generator A U-tubes began to drain, approximately [ ](*AC) seconds later due to the lower fluid steam fraction in hot leg A.

Due to boiling in the rod bundle (data plots 30 and 31), two-phase flow entered the hot leg from the upper plenum and flowed through the PRiiR liX. De flow into the PRiiR IIX consisted of intermittent periods of saturated water and steam which had an average steam fraction significantly greater than the fluid in the upper plenum. The average steam fraction at the PRiiR liX inlet was as high as [ ](*A*) percent, which enhanced the PRIIR liX heat transfer from the primary system, as compared to its heat removal capability with single-phase saturated or subcooled water. When the primary system flow stabilized after the initial now oscillations, a PRiiR liX heat removal rate of

[ ]('A') kW was calculated. This calculation was based on the steam fraction at the PRiiR llX inlet (as calculated from the dP instrument readings in data plot 29), the averaged return flow rate, the llX inlet and outlet temperatures, and the pressure. His calculation, which assumes a slip coefficient of I between water and steam, may be lower than the actual heat transfer and should only be used for test-to-test comparison.

When the primary system pressure decreased to the saturation pressure for the fluid in the upper head, it began to drain (at approximately [ ](*AS) seconds).

When the loop-B cold legs had partially emptied, the CMTs transitioned from their recirculation mode of operation to un intermittent draindown mode of operation at approximately [ ](a.b.c) seconds.

During the first [ ](*AC) seconds of this test (shortly after ADS-1 actuation), [ ](*A*) Ibm of water were expelled through the break draining the: the pressurizer, the steam generator U-tubes, the power channel upper head, the power channel upper plenum above the hot leg, most of the cold legs, mwaxum.nonwc romunmib-oso997 4.2.6-2 Revision: 2

and approximately [ ](a.b.c) percent of the ChtTs. De heated rods that simulate the A.P600 core decay heat reduced power to approximately 230 kW at 4800 seconds. This value consisted of 80 kW N

of decay heat and 150-kW of heat loss compensation. ne mass now rate out of the break was I

decreasing, indicating that cold leg B2 was almost empty.

ne ADS phase began with the actuation of ADS 1 (at approximately [ )(a.b.c) seconds). ADS 2 and -3 occurred within the next [ }<a.b.e) seconds. The heat loss compensation was removed from the rod bundle power decay simulation when ADS 1 occurred, reducing the rod bundle power to approximately 80 kW.

De ADS actuation increased the rate of primary system depressurization and resulted in high l injection flow from the accumulators. The rapid injection of cold water from the accumulators (from

[ ]<a.b.c) seconds) and the ChtT injection flow refilled the power channel / upper plenum, the horizontal portion of the hot legs and the pressurizer. When the accumulator discharge ended, the now through the heater bundle decreased to the injection rate of the Chits and the PRHR HX Dow, and two-phase flow occurred again the heater bundle, hot leg A, the PRHR HX, and into the pressurizer. De rod bundle steam fraction continued to increase (collapsed liquid level decreased) until after ADS 4 was actuated.

, ne mass flow rate through the break decreased sharply at approximately [ )(a.bd seconds, indicating that cold leg B2 emptied and that the break flow was steam. During the ADS phase, approximately [ ](a,b.c) Ibm of subcooled water were discharged from ADS 1, -2, and -3.

ne post ADS period began when ADS-4 actuated. ADS-4 occurred at [ )(a.b.c) seconds, the fluid discharge through ADS 1, -2, and 3 stopped, and the pressurizer water drained back into hot leg-A.

A small amount of ChtT flow continued into the downcomer via the direct vessel injection (DVI) line.

When the primary system pressure decreased below the pressure corresponding to the water elevation head of the IRWST, flow from the IRWST began. Shortly thereafter, the Ch1T flow ended. The flow from the IRWST gradually refilled and subcooled the power channel, restored single-phase water flow through the rod bundle, and partially refilled the upper-upper plenum. The PRHR HX supply line partially emptied at approximately [ ](a.b.c) and the PRHR HX was no longer effective. A steady flow of subcooled water was established from the IRWST into the downcomer, through the power channel, and left the primary system through the ADS-4 flow paths.

This test demonstrated that the heater bundle was fully covered by a single or two-phase fluid at all times during this test (data plots 30 and 31). There was no indication of heater rod temperature increase due to lack of cooling (data plot 3). Key parameters comparing the S01613 test with other tests are listed in Table 51 in Section 5.0.

O mAap6000632wnon\sec 4\3632w-4.non:lb-050997 4,2,63

Discussion of Test Transient Phases

• Initial Depressurization Phase (0 to [ ]<a.be) Seconds)

The initial depressurization phase (IDP) began with the initiation of the break (at time 0) and ended when the primary system pressure reached the saturation pressure of the Duid in the lower upper plenum and the hot legs (Figure 4.2.61). This phase included the following events:

R signal at 1800 psia (decay power simulation initiated and the MSIV closed), and S signal at 1700 psia (the MFWlV closed, the CMT injection line isolation valves opened, and the PRllR heat exchanger return line isolation valve opened-all with a 2-second delay; and RCP coastdown staned after a 16.2-second delay). See Table 4.2.6-1.

Facility Response During the IDP:

From time 0 until the R signal occurred, the primary system pressure decreased due to the expansion of the pressurizer stearn volume caused by fluid loss through the break. The pressurizer partially compensated for the loss of pressure by flashing; however, it was drained after [ }(a,be) seconds (data plot 32). The R (at [ )(n.b.c) seconds) and the S (at [ l'**h) seconds) signals were based on pressurizer pressure only. When the R signal occurred, the MSLIV closed and the power was reduced to 20 percent of full power after a 5.75-second delay and began to decay after a 14.5 second delay.

As a result of the power reduction without flow reduction, the rod bundle AT decreased due to the low power /Dow ratio and the lower-upper plenum temperature dropped toward the cold-leg temperature. At the same time, the primary system pressure had decreased to [ ](a,be) psia (the saturation pressure of the [ ](a,be).F water in the upper-upper plenum), and the upper-upper plenum began to flash and rapidly drain. System pressure decreased to approximately

[ )(*'hd) psia at [ )(n b.c' seconds. At this time, the pressurizer was drained, but primary system pressure was still dictated by the temperature of the saturated vapor m the pressurizer (about [ ](a,b.c).F) and the fluid in the surge line. When the RCPs shut off (at

[ )(a,b c) seconds), the rod bundle and upper-plenum fluid temperatures increased due to the increased power / flow ratio at the lower flow. System pressure increased temporarily until the decreasing rod bundle decay power and the decreasing lower-plenum temperature (due to the CMTs injecting cold water into the downcomer) began to reduce the lower-upper plenum fluid temperature. The decrease in primary system pressure resulted from the balance between the steam generation rate (from flashing primary fluid), the volumetric flow of liquid out of the break, and the steam condensation occurring in the PRHR HX. Steam was continually generated by boiling due to the heater power. As system pressure continued to decrease, more fluid reached its saturation pressure and flashed. 'lhe PRHR HX flow started before the RCPs were tripped and then continued by natural circulation (data plot 37). Primary system pressure stabilized at saturation pressure for the bulk hot fluid in the primary system (approximately $40'F), as shown in Figure 4.2.6-1. This ended the IDP.

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ne flow oscillations in the hot legs reached the steam generators. In stearn generator A, the U4ubes were full until approximately [ ](**#) seconds into the transient. At this time, a U free water surface began to develop in the top of the U-tubes, primarily due to the separation of steam from the two-phase mixture from the hot leg at the low flow velocities existing at natural circulation now conditions. The fluid level on the hot leg side of the U tubes oscillated as it decreased. This condition continued until approximately [ ](**#) seconds into the transient, at which time the top of the U tubes remained filled with saturated vapor and the U tube water level decreased smoothly.

De fluid level on the cold-leg side of the steam generator A U tubes exhibited significant level oscillations from about [ )(*'h) seconds and it appeared that intermittent flow over the l top of the U-tubes occurred. At [ ](a,be) seconds, the U tube water level decreased smoothly and was drained at about [ )(a,b.c) seconds. '

Because of the higher steam fraction of the fluid in hot leg-B and steam generator B, the time over which oscillations occurred was reduced .ind the U-tubes filled with saturated vapor sooner. As a result, the steam generator B U-tubes tv gan to drain at about [ ](**# 3 seconds.

He level in the steam generator B hot leg side U-tubes dropped to near zero at about

[ )(**b#) seconds. De cold leg side U tubes exhibited significant level oscillations from about t

[ J a,be) seconds which continued until the U tubes were drained at [ ]<a,be) seconds (data plots 22 and 23).

. Ilot Legs Hot legs A and B were full of two-phase Guid until ADS-1 was actuated, when the measured level decreased (data plots 20 and 21). He hot legs were nearly drained at ADS 4 ([ )(**d) seconds) and partially refilled after IRWST injection began. De principal difference between hot legs A and B was the influence of the PRHR HX on the void fraction in the hot legs during the PDP. Assuming that the fluid in the hot legs initially had the same steam fractions at the outlet of the power channel lower-upper plenum; the FRHR appears to have preferentially removed steam from hot leg A (as seen in the very high steam fraction for the PRHR inlet flow), thereby reducing the steam fraction of the Guid in hot leg A to less than the fluid steam fraction in hot leg B. The apparent steam fraction in hot leg-A was [ )(**#) percent at [ ](**#) seconds; while in hot leg-B it was [ ](**#1 percent. He hot leg steam fraction affected the draining of the steam generators U tubes, with steam generator-B draining earlier than steam generator-A.

. Cola Legs Cold legs-Al and -A2 remained full until [ )(a,b,c) seconds (data plots 22 through 27), at which time the level decreased to the horizontal section of the pipes and drained at about [ ](**#)

h seconds. When ADS-4 occurred, the water level in the tubular downcomer temporarily dropped reaching [ ](a,be) ft. below the hot-leg elevation at [ ](a,b,c) seconds (data plot 24). The rod mw6aoosn.nonvecau6nwa non m oso997 4.2.6-11

bundle steam fraction fluid increased. After IRWST injection began at [ )(a,be) seconds, the annular downcomer refilled and the cold and hot legs were partially refilled after [ )(a,b,c) seconds to the level of [ )(a.be) ft. above the hot leg.

Cold legs-BI and B2 remained full until [ )(a,be) seconds into the event, at which time both cold legs-B1 and -B2 drained rapidly to the level of the horizontal section of the pipes. 'Ihis reduced water level in cold leg-B1 and cold leg B 2 initiated the transition of the CMTs from their recirculation to draindown mode of operation. Cold legs B1 and B2 were refilled at [ )(* h#'

seconds to the level of [ ](a,be) ft. above the hot leg. At this time, the cold leg to CMT balance lines were partially filled.

• PRHR and IRWST At the initiation of the test, the PRHR HX was filled with subcooled liquid. When the S signal occurred, the PRHR HX isolation valve opened and flow started through the HX at a high flow rate due to the still operating RCPs. When the RCPs were shutoff and the power channel upper plenum and the hot legs filled with two-phase fluid, a large portion of the steam in hot leg-A flowed to the PRHR HX (data plot 29). The two-phase mixture, consisting of attemating slugs of steam and water, was condensed and subcooled in the PRHR HX (data plot 28) from [ )(a,be).p to below [ )(a,b,c).F. During the PDP (prior to ADS 1), there was a significant variation in the flow through the PRHR HX, caused by the variation in the steam fraction in hot leg A. Steam condensation was apparently occurring in the PRHR HX as evidenced by the rapid and wide variations in dP measurements (data plots 28,29, and 37).

After the ADS sequence began, the power channel and the hot legs were refilled with subcooled water by accumulator injection. The driving head for flow through the PRHR HX decreased due to the sharp decrease in the PRHR HX supply line temperature (data plot 19) and the flow decreased.

After accumulator injection flow decreased, the upper plenum and hot leg A again became saturated (data plots 4 and 5), and a two-phase mixture again occurred in the hot legs; the PRHR HX supply line began to drain; and PRHR HX flow rapidly decreased and essentially stopped. In spite of the increasing steam fraction of the fluid in the rod bundle and upper plenum that occurred prior to IRWST injection, PRHR HX flow did not astart.

The heatup of IRWST water resulting from the operation of the PRHR HX is shown in data plot 17. Following ADS-4, primary system pressure decreased to near ambient, and gravity flow due to the water elevation head in the IRWST began injecting water into the annular downcomer via the DVI lines. The flow from the IRWST was sufficient to refill the power channel, downcomer, and loop piping and to establish subcooled fluid flow through the tube bundle and out I through the ADS-4 flow paths (data plots 32 and 40).

O nmaat632.nonssee-413632. 4 non ib-o<m7 4.2.6-12 Revision: 2

. Core h1akeup Tanks G The CMT injection was initiated two seconds after the S signal when the CMT injection line isolation valves were opened. Initially, the now from the CMTs occurred by natural circulation; hot water from cold legs Howed to the top of the CMTs and cold water from the bottom of the CMTs flowed to the downcomer, via the DVI lines, into the power channel.

Initially, this recirculation rate was approximately [ )(**#) Ibm /sec. from each ChfT. De now I rate slowed down to [ )f**#) lbm/sec. at [ )(**#) seconds due to the decreased buoyant head driving force that occurred as the CMT water was replaced with hot water from the cold legs, and as the cold leg water temperature decreased.

After cold legs B1 and B2 drained to the level of horizontal pipes at [ )(a,be) seconds, Dashing / draining began in the cold leg balance line. When the temperature at the top of the CMT reached the saturation temperature for primary system pressure, a free water surface was established in the CMTs. His increased the driving head for the injection Dow and resulted in a I higher draindown flow rate. For the 1 inch LOCA, the break flow at this time was less than full CMT draindown now rate. This caused the CMT injection to consist intermittent short periods of draindown which increased the cold leg water level and short periods of refill with water from the cold legs. This resulted in a slow decrease in CMT levels and the ADS 1 actuation was therefore delayed and occurred at a system pressure of approximately [ )(a,be) psia, considerably below 711 psia accumulator gas pressure. Part of the accumulator coolant inventory was therefore v' injected into the primary system prior to ADS l. His accumulator injection helped maintain the primary system coolant inventory at cold-leg elevation and thus contributed to intermittent CMT draindown/ refill. For test 501613, the transition from recirculation to the draindown mode of operation occurred at [ )(a,b,c) seconds for both CMT A and CMT B as shown in data plot 38.

He CMT balance lines finally completely drained at [ )(8,b,c) seconds (ADS 1), resulting in an increase in CMT injection flow rate. The steam in the CMT balance lines and at top of the CMTs was slightly superheated as the primary system pressure was rapidly reduced by ADS operation.

The CMTs were heated first by the hot liquid from the which replaced the cold water draining from the bottom of the CMTs. A stable, stratified thermal gradient was established in the CMTs (data plots 15 and 16;. Later steam from the cold legs maintained the exposed metal and free-water surface temperatures at or near saturation temperature.

He CMT recirculation mode now rate was initially approximately [ )(a,b,c) lbm/sec. and steadily decreased to approximately [ )(a,be) Ibm /sec. when the transition to draindown began.

The CMT average injection flow rate increased to approximately [ )(**#) IbnVsec. during the transition period. After ADS 1 actuated, CMT injection increased again to ( )<a,be) lbm/sec. and then gradually decreased with time. During the accumulator injection (ADS 1), the CMTs'draindown rate remained high. CMT-A was drained at about ADS-4 ([ )(a,b,c)

()/

N_

seconds). He CMT B injection now rate decreased when the IRWST started at about [ )(**#)

m%p60oJ632*nonhec-40632m-4 non.1b-050997 4.2,6 13

Seconds, and CMT B stopped flowing at [ )(a,b4) seconds and never completely drained (data plots 33 and 38).

• Accumulators ne accumulators provided water injection by a polytropic expansion of a compressed air volume stored within the accumulator. Accumulator injection started when the primary system pressure dropped below 711 psia at 2400 seconds. The accumulator injection now rate was low until ADS 1 was actuated at approximately [ )(a,b,c) seconds when the flow rate increased to approximately [ )(hd) Ibm /sec. The accumulator injection after ADS actuation lasted approximately [ )(a,be) seconds, and the accumulators were completely drained (data plot 34).

l De effective polytropic coefficient of expansion was calculated for the accumulators (Figures 4.2.5 3 and 4.2.5-4) to be [ Jt a,be) for accumulator-A and B. This was near the mid-point between isothermal expansion (k = 1) and adiabatic expansion (k = 1.4) and showed that some heat was picked up by the compressed air from the intemal metal surfaces of the accumulator during the expansion.

l Mass Discharge and Mass Balance The catch tank weight measurements are shown in data plot 43 for the break Dow, for the ADS 1, -2, and 3 flows, and for the ADS-4 flow. The break flow as shown in plot 44, which began when the test was initiated, was stable with a decreasing How rate as system pressure dropped during the IDP and the PDP. When the ADS was actuated, the break location voided, and further discharge from the break was primarily saturated steam until IRWST injection refilled the cold leg after ADS-4.

The discharge from ADS 1, 2, and 3 was stable throughout the accumulator injection and increased temporarily when the injection ended. When ADS-4 occurred, the discharge of Guid from the top of the pressurir.er essentially ended, and the Guid discharge from ADS-4 began. The ADS-4 iluid discharge rate was relatively stable and continued until the end of the test. He discharged masses are shown in Table 4.2.6 4 The mass balance results for test S01613 were calculated based on water inventory before and after the test. Table 4.2.6 2 gives a te' ailed listing of the inventories of water in the various components before the test. Table 4.2.6-3 lists the inventories after the test and the amount of water injected into the vessel from the IRWST. De water level in the vessel was determined by the DP B16P measurement to be [ )(h#)in. (577 mm) above the hot leg centerline at the end of the test. Table 4.2.6-4 compares the mass balance for the system before and after the test and shows 102.6ck agreement of the measurements.

O mww2w=v.ecam w-4mn.tso50997 4.2.6-14 l

_ _ _ _ - _ . - _ ~

TABLE 4.2.61 SEQUENCE OF EVENTS FOR TEST S01613 Event Specified lastrument Channel Actual Time (sec.)

Break Opens 0 Z_001BC (a.b,e)

R Signal P = 1800 psia P-027P l MSL IV Closure R signal + 2 sec. Z_A04SO, F_A04S Z_B04SO. F_BMS t

l SCRAM R signal + 5.7 sec.

S Signal P = 1700 psia P-027P CMT IV Opening S signal + 2 sec. Z_AN0EC. F A40E Z_BNOEC, F-840E PRHR Heat Exchanger S signal + 2 sec. Z_A81EC, F.A80E Actuation (

MFW IV Closure S signal + 2 sec. Z_B0250,F_BOIS 2

Z.A02SO,F_A0lS Reactor Coolant Pumps S signal + 16.2 sec. DP-A00P I

O Accumulators P-027P = 710 psia DP BOOP F_A20E

+30 sec. Z_00!PC ADS 2 CMT level 67% L_B40E

+125 sec. Z_002PC ADS 3 CMT level 67% L_B40E

+245 sec. Z_003PC ADS-4 A/B CMT level 20% L B40E

+60 sec. Z_004PC, F 040P IRWST Injection P-027P = 26 psia F_A60E F_B60E _

O mvan632wnonssec-4\363:w-4 non.1b-050997 4.2.6-15 Revision: 2

TAllLE 4.2.6 2 WATER INVENTORY llEFORE TEST S01613 PRlhlARY SYSTEh!

Volume NetVol Relathe blass Component (ft.3)/(I) (ft.3)/(I) Temp ('F) Density (Ibm) (s.b.c)

Loops 8.97 ft.3 8.97 ft.3 (254.0 h (254.0 I)

Pressurizer 3.37 ft.3 1.82 ft.3 (95.4 I/ (51.6 I)

Surge Line 0.34 ft.3 0.34 ft.3 (9.6 I) (9.6I)

Tubular Downcomer 1.38 ft 3 1.38 ft 3 (39.1 h (39.1 I)

Annular Downcomer + 0.54 ft.3 0.54 ft.3 liigh. Pressure Bypass (15.3 I) (15.3 !)

Core Bypass 0.44 ft.3 0.44 ft.3 (12.4 I) (12.4 I)

Lower Plenum 0.81 ft 3 0.81 ft3 (22.8 I) (22.8 I)

Riser 1.64 ft.3 1.64 ft.3 (46,4 h (46.4 I)

Upper Plenum 1.46 ft.3 1.46 ft.3 I (41.3 I) (41.3 I)

Upper llead 1.90 ft.3 1.90 ft.3 (53.8 4 (53.8 I)

ChlT A 5.05 ft.3 5.05 ft.3 (143.0 0 (143.0 0 ChlT B 5.05 ft.3 5.05 ft.3 (143.0 h (143.0 ()

ACC-A 5.05 ft.3 3.90 ft.3 (143.0 I) (110.4 I) l ACC-B 5.05 ft.3 3.90 ft.3 (143.0 I) (110.4 I) 1RWST Injection Line 0.18 ft.3 0.18 ft.3 (5.10 (5.1 I)

TOTAL PR1hlARY INVENTORY - -

O mup6mu63:wnonwao632 4 non:Ib-osov97 4.2.6-16

4.2.12 Steam Generator Tube Rupture without Nonsafety Systems (S01110)

[

V This matrix test simulated a steam generator tube rupture (SGTR) without any consafety systems operating or operator actions, and with only the automatic passive safety systems used for accident mitigation. The pressurizer internal heaters were shut off at break initiation and the chemical and volume control system (CVCS), normal residual heat removal (NRHR) function, and startup feedwater system (SFWS) were shut off for this test. The single SGTR is simulated via a line connected from the primary side (teactor coolant pump (RCP) B suction piping) to the secondary side of steam generator A (approximately [ ]<a.be) ft. above the tube sheet), with a break orifice diameter scaled to simulate [ )(s.be) times the area of a AP600 steam generator tube.

Results are provided in the data plot package at the end of this section. The sequence of events for S01110 is listed in Table 4.2.121. During mitigation of the SGTR, there was no core makeup tank (CMT) draindown, and no accumulator or in-containment refueling water storage tant (IRWST) injection throughout the transient.

Since this SGTR test did not result in automatic depressurization system (ADS) actuation only the first two event phases observed in loss-of coolant accident (LOCA) recovery occurred. The event phases selected for purpose of detailed evaluation of the non-LOCA events are shown in Figure 4.2.121 and are as follows:

(N . Initial depressurization phase (IDP) - Point I to 2 2

• Pressure decay phase (PDP) - Point 2 to 3 Overall Test Observations

Figure 4.2.121 shows the facility primary system pressure during matrix test S01110 (as measured at the top of the pressurizer) in relation to selected component actuations and other facility responses.

He IDP began with the opening of the break valve between the primary and secondary side, causing the pressurizer to drain. De pressurizer heaters remainer )n after break initiation until approximately 250 seconds, slowing the reduction in pressure due to pessurizer steam expansion. After the heaters shut-off, the reactor pressure decreased at a faster mte until the reactor trip and safety system actuation ocarTed.

Wben the pressurizer level dropped to [ ]<abe) ft. at [ )(a.be) seconds, the textor trip (R) and safety system actuation (S) signals were actuated. [ ](a.be) seconds later, the main steam line isolation valves (MSLIVs) and main feedwater isolation valves (MF%7Vs) were closed, the CMT and passise residual heat removal (PRHR) heat exchanger (HX) retum line isolation valves were opened, and the RCPs coasted down with a ( )(a.be)-second delay (at [ )(a.b.c) seconds into the event). Rod bundle power was reduced to [ ]<a.bx) percent of full power after a [ ]<a.be)-second delay (at [ ](a.b.c) seconds), and the simulated power decay began after a [ ](a.br) second delay. The bundle power wu maintained 150 kW above the scaled decay power to compensate for facility heat losses.

4 O(_/

m \ap6000632wnon\wc-40632w.7.non Itr050997 4,2,12-1 Revision: 2

Re recirculation flow through the CMTs and the PRilR flow began immediately after the isolation valves were opened. The changing rod bundle power to flow ratio caused by the time delays between rod bundle power was reduced. When the RCPs were tripped and coasted down, this reduction caused a sharp decrease, then increase in the hot leg temperature. This reduction also caused a rapid decrease in pressurirer pressure from [ )(*AC) to [ )("AC) psia followed by a slight increase in pressure.

Primary pressure then decreased to the steam generator saturation pressure due to heat transfer to the steam generators. The IDP ended at [ )(a.b.c) seconds, when hot leg / upper plenum temperature

([ ]<a.b.c)*F) started to control the primary system pressure; and break flow stabilized at approximately [ )(a.b.c)lb/sec. (Figure 4.2.12 5). Data plot 31 shows that the level of the upper-upper plenum above the hot legs began to decrease.

During the initial portion of the PDP (up to [ ](a.b.c) seconds), the primary system, with the exception of the upper-upper plenum and upper head, remained water solid. Primary system cooling was provided by the PRHR HX, CMT recirculation, break flow, and facility heat losses. At [ )(ahc) seconds, these were 83 kW, 84 kW,7 kW and approximately 125 kW, respectively (approximately 300 kW total), as compared I

to the heated rod power of 245 kW at [ )("A') seconds. Thus, the primary and secondary system temperature and pressure slowly decreased throughout the PDP. De above PRHR HX heat removal rate l was based on the steam fraction of the flow in the PRHR supply line (calculated to be low at this time, as detemdned from the dP instrument readings in data plot 29) and the PRHR flow rate, HX inlet and outlet tempemtures, and pressure.

As shown in data plot 31, at approximately [ )(a,b.c) seconds the upper-upper plenum and the upper head began to drain at a significant rate. His resulted in an increasing pressurizer level (data plot 32).

The upper upper plenum drained rapidly from approximately [ )(*AC) seconds and was completely drained to the hot leg elevation at approximately [ )(a.b.c) seconds.

At this time, primary system and secondary system pressures were essentially equalized and several events occurred almost simultaneously:

The break flow to steam generator-B decreased from approximately [ )(a.b.c) lbm/sec at

[ )(*AC) seconds to approximately [ )(*A') at [ ]<a.b.c) seconds (Figure 4.2.12 5). Total break flow mass from the primary system to secondary side of cteam generator B was approximately [ )(a.b.c) lbm (Figure 4.2.12 3).

The steam generator-B tubes began to drain at approximately [ ](a.b.c) seconds.

The loop-B cold leg flows decreased and loop-A flows increased momentarily.

Steam voiding began in the rod bundle resulting in two-phase flow through the lower-upper plenum, hot legs, PRHR supply line, etc.

The pressurizer level rapidly increased in response to the draining steam generator-B tubes, upper head, and primary system steam generation.

m u r4000632 m non\sec-4i3632w .7.non. lb-oSO997 4.2.12 2

'Ihis resulted in oscillations of temperature, steam fraction, tubular downcomer flow, and system p

\

pressure, all of which continued throughout the test. The pressurizer was completely filled at

[ ](*A') seconds and remained filled until the test was terminated. The CMT natural recirculation flow continued, but the flow rate was decreasing. The upper head was completely drained at

[ ]("AC) seconds, and the level never recovered. The prirr.ary system pressure oscillated about the secondary system pressure and there was a small alternating flow in the break line.

Due to periodic boiling in the heater rod bundle (data plots 30 and 31), two-phase mixture with wide variations in steam fraction entered the hot leg and flowed to the steam generators and PRiiR llX.

This resulted in attemating slugs of steam and water in the PRHR 11X supply line, which resulted in oscillations in the PRIIP heat removal rate and return flow rate. De oscillating retum to flow into the cold legs and tubular downcomer caused small heater rod temperature oscillations.

liot leg-B fluid had a steam fraction close to that in the lower upper plenum. liowever, the steam fraction in hot leg A was lower due to the selective removal of stearn from the hot leg into the PRliR inlet line. The steam fraction at the PRifR liX inlet oscillated and reached high peaks, which enhanced the PRHR heat removal from the primary system as compared to the heat removal with single-phase saturated or subcooled water before [ ]("AC) seconds.

As stated above, the steam generator-B U-tubes began draining at approximately [ ](*AC) seconds into the event. At the end of the event, the steam generator-B U-tubes were drained, including part of the pump B suction line. The U tubes steam generator A never drained; however, there was an O' oscillating flow with wide variations in steam fraction in the upper section of the U tubes.

This test demonstrated that the heater rod bundle was fully covered (single phase or two-phase mixture) at all times during this test (data plots 30 and 31) and that there was no indication of heater rod temperatures increasing due to lack of ecoling (data plot 3) Also, the passive safety system functions were shown to mitigate the consequences of a SGTR with no operator actions or use of nonsafety systems. Key parameters comparing the S01110 test with other tests are listed in Table 5-1 in Section 5.0.

Discussion of Test Transient Phases

. Initial Depressurization Phase (0 to 1050 Seconds)

The initial depressurization phase (IDP) began with the initiation of the break (at time 0) and lasted until the primary system pressure decreased to the saturation pressure for the upper plenum and the hot legs (Figure 4.2.12-1). This period included the following events: initiation of the break, the actuation of the R and S signals, closure of the MSLIV and MRVlV, opening of the CMT injection line isolation valves, and opening of the PRHR HX retum line isolation valve; all with a [ ](*AC) second delay. Rod bundle power was reduced to [ ](*AC) percent with a

[ ](*AC)-second delay, the rod bundle decay power was initiated with a [ ](*AC) second delay, C Jt a.b.e)- second delay.

and RCP coastdown was initiated after a [

myoco6nwnonwcau6nw-7.ncalt oso997 4.2.12-3 Revision: 2

System Response during the IDP:

ne break was initiated at time 0. From time 0 until the R and S signals were activated (at

[ ]'*AC) seconds), the system lost pressure due to the Guid loss through the break resulting in a j decreased pressurizer level and an expansion of the pressurizer steam bubble. When the trip

{

signals were activated, the power was reduced to [ ]("L') percent of full power after 1

[ ]("AC) seconds. At [ ](*A') seconds, the SPES 2 integrated power from the time of the R signal simulates the AP600 post-trip integrated power. The SPES 2 power was then decreased to simulate the AP600 decay heat plus 150 kW for facility heat loss compensation, which was maintained throughout this transient. The htSLIV was closed at [ ]("A') seconds. As a result of the power reduction without flow reduction, the rod bundle AT decreased, and lower upper plenum temperature dropped temporarily to the lower plenum temperature of [ ](a.b.c).p, ne system pressure decreased to [ ](*AS) psia at [ ]("AC) seconds (Figure 4.2.12-2). At this time, the pressurizer drained and the system pressure was controlled by the temperature of the saturated Guid ([ ](*A*)*F) in the surge line. When the RCPs were shut off (at [ ](*A*)

seconds), the rod bundle and the lower-upper plenum temperatures increased to [ ]('AC)*F,asa result of the increased power / flow ratio for the rod bundle at the lower flow. He system pressure increased temporarily to [ ](*AC) psia until there was a drop in the decay power and there was a reduction in the plenum temperature. The lower plenum temperature was affected by the ChtT cold fluid injection into the downcomer and the PRHR HX flow into cold leg. De pressure decreased at a rate of [ ](*AC) psia /see in this time period (at [ ](*AC) seconds). He Ch1T recirculation flow and the PRHR flow, break flow, and facility heat losses were sufficient to keep the flow through the power channel subcooled.

He PRHR flow started before the RCPs were shut off and continued by natural circulation after RCP coastdown (data plot 37). He pnmary system pressure stabilized at the saturation pressure for the bulk temperature of fluid on the hot leg side of the power channel (approxin's ely 540'F) at [ ](*AC) seconds. This ended the IDP.

Pressure Decay Phase (1050 Seconds to End-of Test)

The pressure decay phase (PDP) began when the primary system pressure (Figure 4.2.12 2) was dictated by the saturation pressure for the hot leg fluid temperature, and continued until the end of the test. This phase was characterized by a slow decrease in the overall system pressure and temperature. The rod bundle power (decay power plus heat loss compensation) reduced from

[ ](*AC) LW to [ ](*A*) kW (data plot 1).

At[ ](aAc) seconds (bundle power [ ](*AC) kW), the PRHR HX heat removal rate was appimimately [ ]("A') kW, the Ch!Ts provided approximately [ ](*AC) kW effective heat removal due to the cold Ch1T water replacing the hot water entenng the Ch1Ts through the balance lines, the break Dow removed epproximately [ )("AC) kW, and facility heat losses were approximately [ ](*AC) kW. Dus, the total heat removal exceeded heat input (299 kW versus 245 kW), there was no boiling in the rod bundle, and primary system pressure decreased slowly.

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' E 1 Objectives r i ne objectives of the error analysis are as follows:

To describe the errors of the measurements ;*rformed during the SPES-2 test program.

To give the rernits of the error analysis calculatior-l he error analysis was perfctmed a metric units; however, the final results are reported in English units.

- E 2 Error Evaluation -

During the test, all measured instrumentation data of the primary and secondary circuit were recorded at a sampling frequency of 2.0 Hz. De recorded data were converted to engineering units (SI) and then plotted versus time. De engineering values were also recorded on magnetic tape in order to transmit the data to Westinghouse Electric Carporation.

E 2.1. Direct Measured Quantities ne direct measured quantities (such as absolute pressures, pressure drops, fluid speed, voltages,

.a

' current, etc.), acquired and recorded by data acquisition system (DAS), were converted into engineering (SI) units using linear formulas:

Y= M * (mV q) 2 K = M = mV + Q where; mV = signal coming from instrument -

M,q

= - calibration constants (q = instrument zero)

-K- = instrument hydraulic head = pte

• g

• h

'Q =-eM*q*K and where:

pLc = water density asyumed at ambient temperature = 1000 (kg/m3) h = pressure tap height difference (m) g =- acceleration due to gravity = 9.80665 (m/sec.2) c To verify that the instrumeat will meet the required accuracy for test, the instruments were controlled g and calibrated in the laboratory before installation in the facility. In the facility, the instrument was ntup60aomwnonupp Enonab-oso997 E-3 Revision: 2

k checked just before the beginning of the experiment in order to control all the T:AS recording channels. He instrument zero was verified daily before staning the test.

Temperatures ne temperature of the fluid, piping, components, and in-containment refueling water storage tank (IRWST) pool water were measured in degrees Celsius by using the following:

Sheated thermocouples type K Cromel-Alumel,0.5- to 1.5-mm OD e

Resistance thermal detector (RTD) thermoresistances type PT 100 A matrix E (mV), T (*C), for K-type thermocouples was generated by the following formula (UNI 7938 specifications):

8 E =( { d T Ii + 125 exp [-1/2 * (T - 127/65)2])/1000 0 1)

I where:

E = electrical signal (mV)

T = temperature (*C) d, = -1.8533 %

• 10'1 di = 3.891834

• 10'3 d2 = 1.664515

• 10 2 d3 = -7.870237

• 10-5 d, = 2.283579

• 10'7 d5= -3.570023

• 10'10 d6 = 2.993291

• 10-13 d7 = -1.284985

• 10-16 dg = 2.223997

• 10-20 The value of temperature T ( C) was obtained from the signals coming from thermocouples E (mV),

performing a linear interpolation of the matrix E T. In the same way, the signals coming from thermoresistances (O) were converted to engineering units (*C) perfonning the linear interpolation of the PT100 type thermoresistance data characteristics generated by the following formula (UNI-7937 specifications):

2 R = 100 * (1 + 3.90802E-3 = T - 0.5802E-6

• T )

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