ML20004E428

Analysis of Two Phase Flow Induced Differential Pressure Across TMI-1 Pressurizer Safety Valve Line Elbow Taps.

ML20004E428
Person / Time
Site:	Three Mile Island
Issue date:	02/15/1981
From:	Croneberger D, Rochino A, Sheu J GENERAL PUBLIC UTILITIES CORP.
To:
Shared Package
ML20004E423	List: ML20004E422 ML20004E426 ML20004E428
References
TDR-240, NUDOCS 8106120171
Download: ML20004E428 (31)

Text

_ _

$gdg TDR NO. _240_ __ REVISION NO. 0 TECHNICAL DATA REPOFiT PROJECT NO. __Q015E_._. PAG 5 1- OF 11

/T

\' PROJECT: DEPARTMENT /SECTION Engineering & Design Three Mile Island Unit 1 (TMI-1) RELEASE DATE 2/6/81 REVISION DATE -

DOCUMENT TITLE:

Analysis of Two-Phase Flow Induced Differential Pressure Arrone TMI-1 Preneuriver h forv Va l vo Linn Elbnu Tnne ORIGINATOR SIGNATURE DATE APPROVAL (S) SIGN ATURE. DATE J.P. Sheu / f ) Qy 1/6/81 g . Rop iny 2[///91 V l i YA T F :

,. v /y l /W APPP.OVgL, pR E)[TERNAL DISTRIBUTION DATE l /h N N-D e DISTRIBUTION l ABSTRACT:

1. Brief Statement of Problem R. C. Arnold Pressure relief valve dif ferential pressure T. G. Broughton l (DP) Transmitters are being installed on elbows C. R. Capodanno '

downstream of the power operated relief valve R. J. Chisholm (PORV), RC-RV2, and the code safety valves, D. K. Croneberger RC-RVlA and RC-RV1B, as shown in Figure 1 in

\ T. M. Dempsey order to detect flow through any of these

{d I. Feinberg R. W. Keaten valves.

inferred.

From flow valve position can be L. C. Lanese G. L. Lehmann The purpose for this analysis is to demonstrate

!* J. P. Moore the adequacy of two phase homogeneous model A. P. Rochino (Reference 3) used for wet steam passing through J. P. Sheu  ;

the elbows, and to calculate the available G. F. Simmons i dif ferential pressure. Mass conservation and D. G. Slear  :. momentum balance were utilized in this analysis E. G. Wallace h with correlation of viscous effect to the R. F. Wilson 'j inviscid solution of single phase and two phase P. R. Clark i induced differential pressures.

I i

l 2. Summary of Key Results j Based on the pressurizer and valve conditions as o shown in Tables 1 and 2, the differential

. pressure's across the elbow taps induced by the single and two phase flows were calculated and tabulated in Tables 3 and 4 with a reactor coolant I.

drain tank (RCDT) pressure at either 14.7 or 70 psia. Viscous effects were considered in the analysis. The difference between the phase separation model and the homogeneous modal was, r.

also estimated for each condition. The height of water column, H 2 , versus mass flow rate, m, for n)

( g the 6" code safety relief valve lines and 4" PokV line was plotted in Figure 5 and 6 respectively.

il

1. 00UU 30 oCOVER PAGE ONLY

_ M i R O 6 1 'L O OI

I TDR 240 Page la 4 U,~

3. Conclusions ,

i From the results of the analyses the following conclusions are reached:

1. The phase separation model is a more realistic model for two phase flow passing through the elbow. This ficw pattern was observed by visualization techniques and depicted in Reference 6. The flow regimes such as slug, annular, intermittent and homogeneous mixturcs described in Reference 8 only exist for horizontal concurrent gas-liquid flows.

2. The maximum dif ference for the height of water column between the separated and the homogeneous models occurs at case B2c, 35% quality of wet-steam in the 4" line elbow with a RCDT pressure at 14.7 psia. For this case the calculated differential pressure using a phase separation model is nigher than that using a homogeneous .* del by 37.5%. The sign and magnitude of difference between J dels depends on the inlet flow conditions.

J 3. Low density fluids with low volume flow rates in the 6" and 4" lines such as case A2d at a RCDT pressure of 14.7 psia, and

]

cases A2c, A2d, and B2d at a RCDT pressure of 70.0 psia induce r% low differential pressures indicating that the heights of

(_sf water column are below 20".

4. The cases tnat produce a d3fferential pressure of less than 20" (A2c, A2d, and B2d at 70 psia and A2d at 14.7 psia) are not of interest since they are well below the conditions of expected operation with only normal makeup being utilized.

Therefore, the elbow tap instruments detect flows in the relief and safety valve tailpipes as low as normal makeup flow for all reasonable conditions.

4. Recommendation It is therefore recommended to install the DP transmitter for detecting flow conditions due to opening of pressurizer PORV and code safety valves.

O

TDR 240 Page Ib h,,

ANALYSIS OF TWO-PHASE FLOW INDUCED DIFFERENTIAL PRESSURE ACROSS TMI-1 PRESSURIZER SAFETY VALVE LINE ELBOW TAPS TABLE OF CONTENTS Page No.

Abstract Title 1 Brief Statement of Problem 1 2 Summary of Key Results 1 3 Conclusions la 4 Recommendation la Section I Purpose and Summary 2 1

II Methods 2 III Evaluation 3 IV Results 12 V Conclusions 12 O VI Recommendation 13 VII References 14 Table 1 Averaged Fluid States in the 6" Code Safety Relief 15 Valve Line Elbow for Different Pressurizer and Valve Conditions.

2 Averaged Fluid States in the 4" PORV Line Elbow for 16 Different Pressurizer and Valve Conditions.

3 Differential Pressure Across 6" Code Safety Relief 17 Valve Line Elbow Taps for Different Pressurizer and Valve Conditions.

4 Dif ferential Pressure Across 4" PORV Line Elbow Taps 20 for Different Pressurizer and Valve Conditions.

fb

\

TDR 240

• Page Ic O TABLE OF CONTENTS (continued)

I Figure Page No.

1 TMI-1 Pressure Relief Valve DP Transmitters 23 2 Phase Separation Model for Two-Phase Flow 24 in the Elbow. ,

, 3 Detail Dimensions of Elbow Cross sectional 25 Area. (R=3b, and 2b=6" and 4" in this Problem) 4 Edge View of Elbow Taps at points 0 and i 26 5 Dif ferential Pressure Across Elbow Taps, 27 Expressed as Height of Water Column, H 2, versus Mass Flow Rate, 5, for the 6" PORV l line 6 Dif ferential Pressure Across Elbow Taps , 28

)7 Expressed as Height of Water Column, H 2e i versus Mass Flow Rate, 5, for the 4" Code Safety Relief Valve Line.

4 I

+

1 i

.__ , - , ... . , _ ..... _,._.,_ , .. - ..... _ .---. _ _._ .. _ . .,_.... . ,.. _ .- -.,_....__ .._. _ ._,_.._ ,_,__ _._._ ~ , _,_, , _._ , ., _ .. _ .

TDR 26 0 Page 2 (N

\~)

I. Purpose and Summary Pressure relief valve differential pressure (DP) Transmitters are being inatalled on elbows downstream of the power operated r;ef valve (PORV), RC-RV2, and the code safety valves, RC-RVIA, anc RC-RV1B (shown in Figure 1) in order to detect flow through any of these valves. As the first step to calibrate DP transmitter, averaged fluid pressure, temperature, quality and mass flow rate at elbow taps under a wide variety of pressurizer and valve conditions were calculated for the 4" PORV line and 6" code safety relief valve lines. The reactor coolant drain tank (RCDT) pressure was taken to be eir.her 14.7 or 70 psia, and steady-state, adiabatic flow conditions were assumed (Reference 1). The pressurizer and valve conditions include saturated steam, saturated water or subcooled water at a pressure of 300, 1000, 2200 or 2500 psig with valves fully open or 10% flow operated (Reference 2).

Based on the averaged fluid conditions, Reference 3 calculated the flow induced differential pressure acrose the elbow taps for one phase (superheated steam or subcooled water) and two phase (wet steam) fluids. The empirical formula in Reference 4 was utilized to correlate the dif ferential pressure across elbow taps for a single phase flow. Furthermore, a homogeneous model was used for 4

two phase flow passing through the cibow in that calculation, i.e.,

wet steam was assumed to be a homo;eneous mixture with a single averaged velocity and mixture properties.

In an attempt to refine the results, an analysis was performed to recalculate single phase and two phase flow induced dif ferential pressure across elbow taps utilizing mass conservation and momentum balance principles (Re ference 5) . A realistic two phase model j considering phase separation in the elbow (Reference 6) was employed '

in this analysis. Furthermore, viscous ef fects (Reference 7) were also considered to realistically correlate the inviscid solutions of dif f erential pressure for single and two phase flows. This analysis also checks independently the adequacy of two phase homogeneous model in Reference 3 and evaluates the pressurizer and valve conditions which will produce measurable indications based on the sensitivity of the dif ferential pressure transmitter.

II. Me thod s The following methods were employed to analyze the differential pressure across the elbow taps:

4

1. Phase separation model as shown in Figure 2 was used for the two phase flow passing through the elbow.

- p G

TDR 240 Page 3 v

2. Euler's and Bernoulli's equations were utilized for each phase to obtain the radial velocity distribution.

3. Interface position of two phase flow at elbow is determined from the quality of wet steam.

4. The differential pressure across cibow taps is obtained considering mass conservation principles and conditions of pressure and velocity continuity at the interface.

5. The two phase solution degenerates to that for one phase of water flow passing through the elbow by setting steam quality equal to zero.

6. The viscous effect for the real flow can be included through correction of the inviscid solution by the method explained in Reference 7.

III. Evaluation A. Dif ferential Pressure Across Elbow Taps for Two-Phase Flow Phase separation model was used for two phase flow passing through the elbow as shown in Figure 2. The liquid phase tends to impinge on the concave wall and form a f.im y ',)

accumulation as observed by visualization techniques in Reference 6. This evaluation is based on the assumption that the liquid droplets outside the liquid film accumula. tion are negligible.

The following steps were followed in the evaluation:

1. Streamline coordinates (s,n) were used on a curved streamline in the elbow as shown in Figure 2. The s axis is along the velocity vector at any point,and the n axis is oriented towards the centec of the streamline radius of curvature. Both s and n axes are in the plane of curvature of the streamline.

2. For water phase in the two phase flow passing through the elbow, the following equations were used:

a. Euler's equation in the n direction is expressed as:

1 Ob L & it .f. R = YY

- l ll)

,-~

v

i TDR 240

p. Page 4 g

38 32 Where: hn : ~) K  ; -

3a represents the cosine of the angle between n axis and negative z axis which is chosen as the direction of gravitational acceleration, g.

dn = - dr; the r axis is directed far away from the center of the curvature (See Figure 2).

? , f and V = fluid pressure, density and axial velocity respectively. ,

Subscript w denotes water phase.

b. Bernoulli's equation at a certain point of the 4 curved streamline i<

( j')

f. 3 2 + 2 = Constant W .

f.

O- Its first derivative with respect to r shows Q

=0 (2) at ( L +3 2) + % 37

c. Water velocity profile es2 he obtained combining equations (1) and (2) as vm = Kr"'

i Where: Kw is an unknown factor to be determined f rom mass conservation and velocity continuity at interface.

d. Mass conservation of w~ iter phase relates water volume flow rate,k, t a water velocity, ,Vu as 9, =

ff f v md A m Aw .

-V

TDR 240 Page 5

,3 b

Where: dA=2./b2 - (r-R)2 dr; A,is the flow cross-sectional area of water phase. The lower and upper limits of integration over dr are r=R+6(55 C and r=R+b respectively. Moreover, ,( is the interface angle, as shown in Figure 3, to be determined from quality, x.

R = radius of curvature as shown in Figure 3. For a standard elbow, R=3h (4)

Vw = water velocity profile as shown in (3).

b = inside radius of the pipe.

rw Thus, the water volume flow rate is found to be:

b

$w = - 2 kw b*ll- CcS'oC)- A {$ 4 Si?l- C0Sd))

N

-t

+dR'-b'{yt2- - SinR(4 bRcosCOSd4 m4 b L )"

,. For steam phase in the two phase flow passing through the elbow, the following equations were used:

a. Euler's equation in the n direction is expressed as

_ _!_ a R + 3, = v/ (g f, a n r Where: subscript s denotes steam ph.se.

b. First derivative of Bernoulli's equation at a certain point of the curved streamline with respect to r yields d '

=0 (7) 3r (f +31)+V)&Y 5

5 g

\

y ,-

, , - e,

_ . - _ _ _ _ _ _ ____._____m _ _ _ _ _ _ _ _ - - -

TDR 240 Page 6 O

1 c. Steam velocity profile can be obtained combining equations (6) and (7) as KA l8)

v, = r

Where: Ks is an unknown factor to be determined from mass conservation and velocity continuity at interface.

4

d. Mass conservation of steam phase relat'se -steam volume j flow rate,Y, , to steam velocity, Vs, as

= v, d A cr's As j.

Where: dA = 2/ b2 - (r - R)2 dr ;A sis the flow cross-sectional area of steam phase.

The lower and upper limits of integr tion over dr are r = R-b and r = R+b COSe(. respectively.

Vs = steam velocity profile as shown in (8)  ;

Consequently, the steam volume flow rate yields

% = -2 K, { - b sir 14 + R Ulit l-cou)-D

't

- RCOSal+b

+] R*- h* { Sin ( R + b cos*Yix)#

4. Interface angle, d , can be derived from quality, x, as follows:

a. Quality x, is defined as m, f, ( V, / %) l 9,)

c x= =

'% * *s Sw t 9, L4s / %)

l O

l

TDR 240

! Page 7' 4

O Where: f,y and m denote fluid density, volume and t- mass in the elbow.

With the assumption that quality, x, is constant through the elbow, the above equation can be rewritten as 4, ( As /Aw)

X= (to)

L+ Ts L As /AJ Where: A w and As denote cross-sectional area of water and steam phase respectively in the elbow.

! b. The total cross-sectional area in the elbow as shown in Figure 3 is:

Au+As = Tt b2 (11)

c. The cross sectional area of water phase, A w, is j determined by eliminating As from Equations (10) and I (11). Thus, KY (12)

O 4 = ' r, gv-v ,

Meanwhile, Au can be obtained from Figure 3 as 4

i 4 = o,5 [ ( l o( - fi/124) (13)

! d. Consequently, interface angle, d , can be implicitly determined from quality, x, by equating (12) and (13).

I 2K 2 4 - filt 2d = (14) i l+ E#

fj ( I - K)

5. Fluid velocity and pressure are continuous at interface between water and steam phases. This condition is expressed as 1

= [ v, u4')

, ( v ] Y = R+ b COS 4 Y = R + b COS4 Consequently, K w =K s =K (15)

(s with aids of equations (3) and (8).

\.j

TDR 240

,x Page 8 Futhermore,

+-

7,=P, w S (10)

Where subscript i denotes interface position.

6. The unknown, K, can be determined considering mass conservation for the two phase flow, g+ k=

g (16')

{ .

Where V , k and Y*s denotes total fluid volume flow rate, volume flow rates of water and steam phase respectively.

With reference to ' Equations (;) and (9), K can be expressed as k (17)

K= n ( R-Jn'-b' )

( 7. Using (3) and (15), Equation (1) can be integrated to yield the

( dif ferential pressure between outside elbow tap and interf ace. ,

Thus, Yo o 1 k

d( ^*9*)= r' dr (1,)

i r, Where subscripts O end i denote outside elbow tap and interface positions respectivoly.

Simplification of (17') results in the relation, fg, - fg, = - fw ( (

~

)Yh(*~' (18)

()

TDR 240 Page 9 7

G]

Where: ro=R+b (19) r1 = R + b COS.( (20)

Z0-Z1 = b (1 - COSo() Sin (90' - 22.3')

= 0.9239 b (1-COSaO(See Figure 4.) (21)

8. In similar developments and utilizing (8) and (15), Equation (6) can be integrated to yield the differential pressure between interface and inside elbow tap. Consequently ~,

1. % 2 dL +32) =

[

tg dr z2;;

i Where subscript i denote inside elbow tap position.

After simplification, the above equation becomes y, - gz=-f( g ( 2) Y 3 (I -*i s

(22) t U) Where ri = R-b (23) zg - zi = 0.9239 b (1 + COS 4) (Tss Figure 4.) (24)

9. Adding (18) and (22) and using (16) gives the differential pressure across the elbow taps for a two phase flow.

2 Pw,- Pse = - t [4 (ii - p) + 3 (z,- z,g (23)

- f, ((( $ - () 4 S c z. - zo]

c

(,A

TDR 240 s

page 10 (a'-

Differential pressure across elbow taps can also be expressed as the height of water column, H, in the DP transmitter,

" ~

H= (26) wb Where: fy = water density in the water column.

B. Differential Pressure Across Elbow Taps for One-Phase Flow The expression for differential pressure across elbow taps due to two phase flow can be reduced to that for single phase flow (sut. cooled water or superheated steam) by setting x = 0 (or.(=K ) or x = 1 (or c( =

0) in the Equation (25). Hence, 1

- (( = f (

) i ) (Zi - 2, ) (27)

Wheref=densityofsinglephasefluid(subcooledwaterorsuperheated steam) 3 Equation (27) can also be applied to the homogeneous model of two phase (d flow passinh through the elbows by using wet steam sensity for f .

Thir, density is expressed by the relation, (27) f = {Vw+i(V-%;)] s Where tru and Vs denote specific volumes of water and steam phase respectively.

C. Consideration of Viscous Ef fects

1. Dif ferential pressure across elbow taps considering viscous effeet for a water flow (Renolds number = 500) passing through a horizontal elbow (R=3b) can he obtained from Figure 6 of Re ferenc e 7 as,

~Po- h h - Pu __ o f7 (28)

S %$, max S Y ,tnmax 2 2

,8 i i L/

TDR 240 Page 11 O -

1 Where subscripts in and max imply conditions at inlet of elbow i and maxismim respectively.

Mass conservation requires that Y in, msg = 2 V in, nva = 2. flK b i

Where Vin, max, Vin, ave denote maximum and averaged velocities respectively at inlet of elbow.

Substituting (29) into (28), differential pre'ssure across elbow taps becomes 2

! f f, - f; = 0. ll55 (30) i 2. Differential pressure across elbow taps for inviscid flow of

! water passing through a horizontal elbow with R

• 3b can be obtained f rom (27) by dropping the. gravitational term, f 3 (Zi -20). Consequently, j .2 f , - f; = 0. 0 8 0 ]

^

~O l 3. The discrepancy between the viscous anc. the inviscid solutions l- of differential pressure across elbow taps for a water flow can be determined by comparing equations (30) and (31) under the i same fluid conditions, f and 9 ant cibow size, b and R.

Consequently,

( Pa - Pd viscous

- ( Po - h invos

). . td , g o, g g (3;*y

! ( P* - N* Viscous This shows that the inviscid flow solution underestimate the

! differential pressure across elbow taps by 30.1%.

4. This correction factor was utilized to correlate the inviscid I solution of differential pressure across elbow taps for two phase, superheated steam, and water flows.

I i

I, O .

'.______________._______._1.______

TDR 240

, Page 12 w]

I V. Results Based on the pressurizer and valve conditions shown in Tables 1 and 2, the differential pressures across the elbow taps induced by the single and two phase flows were calculated and tabulated in Tables 3 and 4.

Rese are provided for the 6" code safety valve lines and 4" PORV line with a RCDT pressure at either 14.7 or 70 psia. Viscous ef fects were considered in the analysis. The difference between the phase eeparation model and the homogeneous model was also estimated for each condition.

Notations in Tables 3 and 4 are explained as follows:

x = quality, mass fraction of steam phase in the wet steam zone.

4 = mass flow rate

= volume flow rate c4 = interf ace angle for steam and ater phases in the wet steam zone, 111= height of water column indicating dif ferential pressure , d P, ,

across the elbow taps. This was obtained for a two phase homogeneous model.

H2= height of water column indicating differential pressure, o f, ,

across the elbow taps. This was obtained for a two phase separation model.

The height of water column, H 2 , versus mass flow rate, m, for the 6" code safety valve lines and 4" PORV line are plotted in Figures 5 and 6 respectively. The signs "+" and "x" represent a RCDT pressure at 14.7 psia and 70.0 psia respectively.

l V. Conclu s ion s From the results of the analyses the following conclusions are reached:

l 1. The phase separation model is a more realistic model for

) two phase flow passing thraugh the elbow. This flow pattern was I

observed by v sualization techniques and depicted in Reference i

) 6. The flow regimes such as slug, annular, intermittent and i

homogeneous mixture: described in Reference 8 only exist for l horizontal concurrent gas-liquid flows.

l l 2. The maximum difference for the height of water column between the separated and the homogeneous mouels occurs at case B2c, 35%

j quality of wet-steam in the 4" line elbow with a RCDT pressure at 14.7 psia. For this case the calculated dif ferential

! (V) pressure using a pha:e separation model is higher than that using a homogeneous model by 37.5%. The sign and magnitude of difference between models depends on the inlet flow conditions.

l l

l_-__--____________--___-----------------------------------------------------^----------^--'^---~^^---'-'--~~^-~~-~^^-~--~

TDR 240 Page 13 7.

(_ / 3. Low density fluids with low volume flow rates in the 6" and 4" lines such as case A2d at a RCDT pressure of 14.7 psia, and cases A2c, A2d, and B24 at a RCDT pressure of 70.0 psia induce lou differential pressures indicating that the heights of water column are below 20".

4. The cases that produce a differential pressure of less than 20" (A2c, A2d, and B2d at 70 psia and A2d at 14.7 psia) are not of interest since they are well below the conditions of expected operation with only normal makeup being utilized. Therefore, the elbow tap instruments detect flows in the relief and safety valve tailpipes as low as normal makeup flow for all reasonable conditions.

VI. Recommendations It is therefore recommended to install the DP transmitter for detecting flow conditions due to opening of pressurizer PORV and code safety Valves.

4

TDR 240 Page 14

~\

l t

%.J VII. References

1. GPU TDR No. 117, " Evaluation of Fluid Conditions at the DP Transmitter on the Pressurizer Relief Valve Discharge Lines," by GAI, May 29, 1980.

2. GPU TR No. T1-0027, Project: TMI-1/RM-10, " Monitoring of Pressurizer Relief Valves," by G. R. Capodanno, August 23, 1979.

3. GPU Calculation No. 1101X-322B-001, "RM Calculation of Differential Pressure Across Elbow Taps," by Richard J.

Chisholm, Jaauary 19, 1980.

4. " Principles and Practice of Flow Meter Engineering," L. K'.

Spink, 1973. ninth edition, The Foxboro Company.

5. GPU Calculation No. 1101X-322C-A07, "Two-Phase Flow Induced Differential Pressure Across the TMI-1 Pressurizer Safety Valve Elbow Taps ," by J. P. Sheu, Augus t 12, 1980.

6. " Transport Processes in Boiling and Two-Phase Systems," Y. Y.

Hsu and R. W. Graham, 1976, McGraw - Hill Book Company.

7. "Two-Dimensional Laminar Flow in Elbows," P. Oxlandt and D.

s Cunsola, Transactions of the ASME, Vol. 101, P. 276-183, June, k's / 1 c /9.

8. Two-Phase Transport and Reactor Safety, Veziroglu, T. N. and Kakac, S. (editors), Proceedings of the Two-Phase Flow and Heat Transfer Symposium - Workshop, " Observation and Correlation of Flow Pattern Transitions in Horizontal Concurrent Gas-Liquid Flow," W. G. Choe, L. Weinburg, and J. Weisman, Vol. 4, p.

1357-1393, October 18-20, 1976, Fort Lauderdale, F1., Hemisphere Publishing Corp. , (1978) .

77 N.J

O O, ,O Dhle 1 .6" Line Static'Presqure @ Tap (PSIA) Static Quality 0 Tap .

RCDT(1^ Pressure Q . RCDT Pressure @ Hass Flow Rate Case Description 14.7 PSIA 70 PSIA 14.7 PSIA 70 PSIA (Ibm /hr)

~ ~ ~

A Saturated Steam l'. Full Flow -

a. 2500 PSIG 387 387 0.85 0.85 322,370 -

.b. 2200 PSIG 333 333 0.89 0.89 275,275

c. 1000 PSIC 143 ,

148 0.99 .

0.99 .

117,925

d. 300 PSIG 46 79 1.0(326*F) 1.0 (346*F) 36,494

2. 10% Flow

a. 2500 PSIC 40 77 0.91 -

0.90. 32,237 2200 PSIC 0.94 . - 0.93 - 27,528

b. 35 '

75 .

c. 1000 PSM 22 72 ' 1.0(299*F); l' .0 (325'F) ' 11,793

d. 300 PSIC 17 70 1.0(324*F)~ 'l.0(345*F) . 3,649

3. 10% valve Rated Flow

a. 300 PSIC 40 76 1.0(324*F) 1.0(345*F) 31,170 B Saturated Water.

J. Full Flow , .

a. 2500 FOIG -

486 486 0.38 0.38 '

654,260

b. 2200 PSIG .

446 446' O.34 s 0.34 634,510

c. 1000 PSIG 244 244 0.21 0.21  :

458,000

d. 300 PSIG -

84 -

101 -

0.'13 't '0.11 . 257,255

2. 10% Flow .

.., ~

. a. 2500 PSIG 49 '

81 O.52 0.50- '

. '65,426

b. 1200 PSIC 45 80 0.49 0.46 ,: 63,451

c. 2000 PSIG 28 .

73 ' ~ 0.35 0.30 _. f 45,800

d. 300 PSIG 19 70 0.21 O.14 ,'

25,726

3. 10% Valve Rated Flow '

a. 300 PSIG 28 72 ,

, 0.19 0.14 .

65,015 C Cold Water

1. Full Flow ,

a. 500 PSIG 140 ' 182 ,. 0.0(200*F) 0.0(200*F) 2,763,154 RCDT@l4.7 yy 2,597,185 RCDTG70.0 g :=

'(1)' Reactor Coolant Drain Tank- . s%

uo TABLE 1 - Averaged Fluid States in the 6" Code Safety Relief Valve Line Elbow for Different Pressurizer and Vt.lve Conditions

O O -

O Table 2 - 4" Lina Static Pressure G Tap (PSIA) Static Quality G Tap -

RCDT(1) Pressure G Mass Flow Rate Case Description 14.7 PSIA 70 PSIA 14.7 PSIA 70 PSIA (lbm/hr)-

A Saturated Steam

1. Full Flow

a. 2500 PSIC 287 286 0.86 0.86 110,960 '

b. 2200 PSIG 248 268 0.89 0.89 94,750 '

c. 1000 PSIC 104 124 1.0(331*F) 1.0(344*F) 40,590

d. 300 PSIC 37 77 1.0(323*F) 1.0(346*F). 12,561

2. 10% Flow -

a. 2500 PSIG' 31 74 0.92 0.90 11,096

b. 2200 PSIG 29 73 0.95 0.93 ' ' 9,475

c. 1000 PSIC 19 71 1.0(299'F) 1.0(325'F) 4,059

, d. 300 PSIG 16 70 1.0(323*F) 1.0 (345* F) 1.257

3. 10% valve Rated Flow

a. 300 PSIG 31 75 1. 0 (321*.") 1. 0(346*F) 10,000 B Saturated k'ater

1. Full Flow j a. 2500 PSIG 402 402 0.39. ~ 0.19 x 225,200 t

b. 2200 PSIC 370 369 0.36 .- 0.36 ..

218,400

c. 1000 PSIC '

189 -

203 0.23 ..

0.22 -

157,650

d. 300 PSIG 74 -

91 0.14 0.12 88,573

2. 10% Flow .

a. 2500 PSIG 41 -78 0.53 i!. 0.50 .I ~22,520

b. .2200 PSIG 38 77 0.49 '. 0.46  : ~f -

21.840

c. 1000 PSIG 24 , 72 0.35 , ,, 0.30 , , .

15,765

d. 300 PSIG 17 69 0.22 ,: 0.14 .k.. . 8,857

3. 10% valve. Rated Flow

$;h '.' .

a. 300 PSIC 23 71 0.20 ~ C.14..8.',f .22,072 .

,OE1 1-I C Cold L'ater .i . .

, j[ ' i." i c- #

1. Full Flow ,i'  : .i 3 '2

~

a. 500 PSIG 161; 201' O.0(200*F)'. .' ,4 0.0(200*F) ;- 1,190,478 RCDT@l4.7

1,118,972 RCDTG70.0~

YY c .=

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Fi g u re 5 - Dif f erential Pressure Across Elbow Taps, Expressed as Height o f Wa te r Col onn.ll, ver. sus Mau Flow Rate. Ih. for t he 6" PORV 1 ine

PAGE 28

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