ML21133A053
| ML21133A053 | |
| Person / Time | |
|---|---|
| Site: | Limerick  |
| Issue date: | 04/29/2021 |
| From: | Exelon Generation Co |
| To: | Office of Nuclear Reactor Regulation |
| Shared Package | |
| ML21138A803 | List:
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| References | |
| Download: ML21133A053 (17) | |
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LGS UFSAR APPENDIX 6A - SUBCOMPARTMENT DIFFERENTIAL PRESSURE CONSIDERATIONS 6A.0 INTRODUCTION NOTE: The subcompartment differential pressure inputs values and analysis results presented in this section for the recirculation line and feedwater line breaks are based on the original design basis conditions. The blowdown mass and energy releases for the recirculation line and feedwater line breaks were reanalyzed at power rerate conditions. Based on the power rerate analyses, the original analyzed load bounds rerate conditions. Therefore, the shield wall design is not affected by power rerate.
The drywell head region pressurization analysis presented in this section was reanalyzed for power rerate conditions. The resulting pressure differential at power rerate conditions is well below pressure differential for the drywell head region.
Differential pressure analyses were performed for the RPV shield annulus and the drywell head region.
The RPV shield annulus, which is 48.95 feet high and 1.70 feet wide at the top, has the 28 inch recirculation pumps suction lines passing through it. The mass and energy release rates from a postulated recirculation outlet line break constitute the most severe transient in the reactor shield annulus. Therefore, this pipe break is selected when analyzing loading of the shield wall and the RPV support skirt for pipe breaks causing annulus pressurization. The estimation of mass and energy release is based on the guidelines set forth in GE's "Generic Annulus Pressurization Mass-Energy Release Methodology" (MFN178-78) and "Technical Description Annulus Pressurization Load Adequacy Evaluation" (NEDO-24548/78NED302). Table 6A-1 presents the full mass and energy release data estimated by applying the finite break opening time/instantaneous break opening time approaches. Because the break location is more than three-fourths of the distance through the penetration, it is conservatively assumed that 50% of the blowdown is released into the annulus, and the remaining 50% is vented to the drywell atmosphere. Table 6A-2 provides, as a function of time, the mass flux and areas used for each side of the break. Physical parameters pertinent to the blowdown rate estimation are noted in the table.
In addition to the analyses for the recirculation outlet line break in the annulus, similar analyses using the same methodology for blowdown rate estimation are performed for a postulated feedwater line break in the annulus. Table 6A-3 presents the mass and energy release rates generated by only applying the very conservative instantaneous break opening time method.
Also, it is conservatively assumed in the analyses that the full blowdown is completely released into the annulus. The mass flux as a function of time and areas used for each side of the break are presented in Table 6A-4. Pertinent physical parameters are noted in the table.
Because the main steam lines are not inside the annulus and the recirculation inlet lines are smaller than the outlet lines, the annulus pressurization analyses for these two cases are not needed.
In considering the drywell head region, the maximum blowdown rate stems from a break in the RHR head spray line. The blowdown mass and energy release rates for this line are calculated 2
using Moody Critical Flow of 2800 lbm/sec-ft and an enthalpy of 1192 Btu/lbm for the original power level. Pressurization consequences at 3527 MWt are based on the original effects and a multiplier. This multiplier is calulated from the effects of the 3527 MWt on the blowdown mass and energy release rates.. Table 6A-5 shows the blowdown schedule for a 6 inch Schedule 80 line break with an effective break area of 0.181 ft2. Since this line could singularly pressurize the drywell head region, it is chosen for analysis in a postulated break. The head spray line does not APPENDIX 6A 6A-1 REV. 17, SEPTEMBER 2014
LGS UFSAR exist for Unit 2 and has been removed from Unit 1. However, the analysis is still applicable since it envelopes loads from rupture of any other pipe in this region.
All differential pressure analyses were performed according to the analytical techniques described in Reference 6A-1. These adjusted pressures are combined with the other appropriate loads (e.g., seismic and jet impingement) to develop design loads for the affected structures and components. Subcompartment venting is used to ensure that the differential pressures developed will remain below the structural capability of compartment walls.
Mass and energy release rates using the NEDO-20533 methodology for a recirculation line break are shown in Table 6.2-10. Short-term release rates based on NEDO-24548 are shown in Table 6A-1. Comparison of these two tables indicates that mass flow rates and enthalpy calculated using NEDO-24548 are less than the conservative values produced using assumptions consistent with NEDO-20533.
Recirculation line break blowdown data used for containment analysis are based on assumptions and calculations made specifically for the LGS units. These assumptions and calculations are discussed in NEDO-10320 (Reference 6.2-5), which follows the methodology outlined in NEDO-20533. This model has been shown to be quite conservative for long-term containment analysis.
However, for the special cases required to analyze pressurization of the annulus due to a recirculation line or feedwater line break, a more detailed model is used. The NEDO-24548 model for short-term mass and energy release includes the effects of inventory and subcooling for flow rates during the first 5 seconds. Credit may also be taken for a finite break opening time.
Blowdown rates from NEDO-24548, which calculates the maximum quasi-steady mass flux based on the Moody steady slip flow model with subcooling, are also considered to be conservative estimates of the mass and energy released from the vessel.
6A.1 BIOLOGICAL SHIELD ANNULUS SUBCOMPARTMENT MODELING PROCEDURES AND ANALYSIS NOTE: The subcompartment differential pressure inputs values and analysis results presented in this section for the recirculation line and feedwater line breaks are based on the original design basis conditions. The blowdown mass and energy releases for the recirculation line and feedwater line breaks were reanalyzed at power rerate conditions. Based on the power rerate analyses, the original analyzed loads bound rerate conditions. Therefore, the shield wall design is not affected by power rerate. The drywell head region pressurization analysis presented in this section was reanalyzed for power rerate conditions. The resulting pressure differential at power rerate conditions is well below pressure differential for the drywell head region.
An analysis was performed of the pressure distribution around the RPV after a recirculation line break. The general layout of the shield annulus is shown in Figures 3.8-1 through 3.8-8 and in 6A-1. Figure 6A-2 is a schematic of the RPV shield annulus model. The model consists of six o
major levels. Each level is subdivided into twelve 30 segments to form a total of 72 nodes inside the annulus plus an additional node for the rest of the drywell.
The guidelines of GE's "Generic Annulus Pressurization Load Adequacy Evaluation" (NEDO-24548/78NED302) were followed in treating the entire drywell region (volume number 73) as a single compartment in the RPV shield annulus subcompartment analysis. Treating the drywell region as a single compartment reduces the drywell pressure response due to venting from the annulus, resulting in the greatest P across the shield wall.
APPENDIX 6A 6A-2 REV. 17, SEPTEMBER 2014
LGS UFSAR The 235,200 ft3 size of the drywell region used in the analysis is a "free volume." The volume occupied by equipment, structures, and floors (i.e.; obstructions) contained within the drywell was excluded from the "free volume" estimate.
In general, the arrangement of the pipes in the annulus determines the most representative level division, since they constitute the only significant flow restrictions. This 73 node model is considered detailed enough to conservatively predict the maximum pressure loads on the compartment structure. Therefore, a nodalization sensitivity study is not needed.
For the purpose of determining peak pressure in the reactor vessel shield annulus, all insulation is assumed to move flush against the biological shield wall while still maintaining its original thickness. The volume of the insulation is excluded from the net volume of each subcompartment, and the projected area of the insulation that blocks the venting path is also excluded from the free venting area used in the analysis.
Venting to the drywell atmosphere is achieved only through the top of the biological shield annulus. For conservatism, venting through the reactor shield wall is not considered.
Initial conditions used in this analysis are 15.45 psia, 135oF, and 30% relative humidity. Bases for these initial conditions are discussed in the drywell head region subcompartment analysis (Section 6A.2).
Tables 6A-6 and 6A-7 give the subcompartment volumes, flow areas, length/area (L/A) ratio, and flow coefficients (including origins) used in the analysis.
The resultant pressure distributions are shown in Figure 6A-3 for the recirculation outlet line break and Figure 6A-4 for the feedwater line break. The subcompartment pressures existing in each subcompartment at the time of peak differential pressure across the RPV are also shown in these figures. Additionally, the load forcing functions that include both peak and transient loadings on the RPV and the reactor shield wall are presented in Figures 6A-5 and 6A-6 for the recirculation outlet break and in Figures 6A-7 and 6A-8 for the feedwater line break. This forcing function represents the time-dependent resultant force on the structure and originates from the vector sum of the product of compartment pressure and area for each of the many nodes used to represent the surface.
The components of these nodal areas are calculated in the following manner:
(Ax)i = Ri Hi Sin ( - ) (EQ. 6A-1) 1i 2i (Ay)i = Ri Hi Cos ( - ) (EQ. 6A-2) 2i 1i where:
th Ri = Radius of the i geometry node, in Hi = Height of the ith geometry node, in
+ = Swept angle of geometry node i 1i 2i Therefore, the force generated by a pressure, (P), acting on a nodal area (A) has the following components:
APPENDIX 6A 6A-3 REV. 17, SEPTEMBER 2014
LGS UFSAR (Fx)i = Pj (Ax)i (EQ. 6A-3)
The compartment pressure transients resulting from a break in the reactor shield annulus generate a nodal force distribution over exposed surfaces. The resultant of this nodal force distribution is presented in Figures 6A-5, 6A-6, 6A-7 and 6A-8. This nodal force distribution is included in the analysis of nonaxisymmetric loadings on the containment internal structures, which is discussed in Sections 3.8.3.3 and 3.8.3.4.
Blowdown jet loads that include jet impingement and reaction forces against the reactor vessel are also analyzed for the feedwater line break for reference and comparison. Note that these analyses are based on the very conservative assumptions that the first pipe restraint nearest the nozzle fails. For this break, approximately 9.5" pipe center line offset limited by the shield plug opening produces a net break area of 88.53 in2, which consequently results into a total maximum jet load against the vessel and a maximum reaction force of 158,500 lbf and 93,230 lbf, respectively. Note that this blowdown jet load is relatively small compared with the peak load contributed by the unbalanced reactor annulus pressurization due to the same break.
6A.2 DRYWELL HEAD REGION SUBCOMPARTMENT ANALYSIS The design basis pressure differential between the drywell head region and the rest of the containment is a structural requirement of the drywell head. A pressure analysis of the drywell head region for a postulated head spray line break was performed. The effects of a 6 inch RHR head spray line break bound those of a 2 inch core vent line, which is the only other line that runs through the drywell head region.
Figure 6A-9 illustrates the basic arrangement of the head region. Venting from the head region is accomplished through ventilation openings as shown in Figure 6A-9. These vent openings provide a total of 18.64 ft2 of vent area with a flow coefficient of 0.64 to relieve pressure buildup caused by the postulated break. Figure 6A-10 is the schematic flow diagram with vent flow areas and discharge coefficient used in the drywell head venting analysis.
For the drywell head region subcompartment analysis, the possibility that insulation from the RPV could break loose and block the vent paths was not considered because the postulated rupture of the RHR head spray line is outside the insulation above the top of the RPV. The jet from the vessel side of the break is above the top of the insulation, which precludes the metallic insulation sections from breaking loose due to the outward flow of the jet. Forces on the insulation from flow from the other side of the break as well as from the subsequent pressurization in the drywell head region would be inward toward the RPV, rather than outward toward the vent paths.
There is only a small amount of insulation on the drywell head region lines. In the event that this insulation should fail to remain on the pipe due to direct jet impingement, the vent paths leading from the drywell region would not become blocked for the following reasons. The openings of each of the six vents and two exhaust lines from the drywell head region are above the floor and have a 3/4 inch mesh screen installed over them. To block the vent paths, a substantial amount of insulation would need to fall directly onto the vent path opening and break through the screen.
This is considered improbable because there is only a small amount of pipe insulation in this region and not all of the failed insulation would fall on any one vent path opening.
APPENDIX 6A 6A-4 REV. 17, SEPTEMBER 2014
LGS UFSAR To determine peak pressure in the drywell head, all insulation is assumed to remain in place.
Initial conditions of 15.4 psia, 135oF, and 20% relative humidity are used in this analysis.
The initial conditions used for both the RPV shield annulus and drywell head region analyses reflect conservative assumptions to minimize the total heat capacity of the subcompartment, which satisfies SRP Section 6.2.1.2, Item II.B.1. The COPDA (NE699/D2) subcompartment analysis code is designed to handle realistic conditions. Recommended minimum relative humidity for COPDA, which is described in Reference 6A-1, is in the range of 25% to 30%. The available heat capacity at P=15.45 psia, T=135F, and RH=30% is less than 3% greater than the heat capacity at 14.8 psia, 135F, and RH=0%, and will not significantly affect the results of the analysis.
The initial pressure of 15.45 psia (0.75 psig) is the nominal drywell pressure under normal operating conditions for this unit. The pressure alarm setpoints are at 14.8 psia (0.1 psig) and 16.2 psia (1.5 psig). The heat capacity gain due to the higher initial pressure of 0.75 psig is less than 0.2% compared to the heat capacity available for T=135F, RH=30%, and P=14.8 psia.
The drywell air cooling system is designed to limit the maximum average bulk temperature in the drywell to 135F, with local maxima not exceeding 150F (Section 9.4.5.2). For a given relative humidity, an increase in the initial temperatures is accompanied by an increase in the steam partial pressure. Consequently, the heat capacity in the compartment increases due to a greater steam mass. For this reason, the maximum bulk temperature of 135F is used rather than the 150F local maximum.
For the RPV shield annulus subcompartment analysis, it should be noted that Reference 6A-2 concludes that loads from such annulus pressurization analyses are insensitive to minor variations in initial (P), (T), and ().
The pressure transient of this analysis is presented in Figure 6A-11. It can be seen that the maximum pressure in the drywell head region is 25.91 psia and occurs 0.82 seconds after the head spray line break. The maximum pressure of 25.91 psia includes an increase of 2.61 psia as a result of power rerate. Considering the containment pressure to be atmospheric (no drywell air displaced into the rest of containment), a differential of 11.2 psid is obtained between the drywell head and the rest of containment. This pressure differential is well below the design pressure differential of 16.0 psid.
6A.3 REFERENCES 6A-1 "Subcompartment Pressure Analyses," BN-TOP-4, Rev 1, Bechtel Power Corporation, San Francisco, California, (November 1972).
6A-2 NUREG/CR-2633, "Containment Reactor Cavity Subcompartment Analysis Procedures for a Boiling Water Reactor", (May 1982).
APPENDIX 6A 6A-5 REV. 17, SEPTEMBER 2014
LGS UFSAR Table 6A-1 REACTOR PRIMARY SYSTEM BLOWDOWN FLOW RATES AND FLUID ENTHALPY - RECIRCULATION LINE BREAK TIME MASS ENTHALPY (s) (lbm/s) (Btu/lbm) 0.000 0.0000 0.000
-3 2.5500x10 1.3400x103 527.9 3.9000x10-3 2.6750x103 527.9 4.9600x10-3 4.0100x103 527.9 5.8600x10-3 5.3500x10 3
527.9 7.3700x10-3 8.0200x103 527.9
-3 9.2400x10 1.2025x104 527.9 1.1800x10-2 1.9285x104 527.9
-2 1.3800x10 2.6560x104 527.9 1.5800x10-2 3.2355x104 527.9 1.8000x10-2 4.5975x104 527.9
-2 4 2.0800x10 4.5975x10 527.9
-2 2.0800x10 2.2400x104 527.9 2.1800x10-2 2.4130x10 4
527.9 2.2800x10-2 2.5840x104 527.9
-2 2.3800x10 2.7520x104 527.9 2.5800x10-2 3.0780x10 4
527.9
-2 2.7800x10 3.3880x104 527.9 3.0800x10-2 3.8170x10 4
527.9 3.5800x10-2 4.4220x104 527.9
-2 3.7000x10 4.5975x104 527.9 4.1400x10-1 4.5975x10 4
527.9 4.1400x10-1 3.4370x104 527.9 1.0000 3.4370x104 527.9 NOTE: The information presented in this table is based on original plant conditions. The values in the table do provide a reasonable representation of the general blowdown characteristics.
APPENDIX 6A 6A-6 REV. 13, SEPTEMBER 2006
LGS UFSAR Table 6A-2 RECIRCULATION OUTLET LINE BREAK BLOWDOWN MASS FLUX TIME HISTORY(1)(2)
EFFECTIVE TIME (s) MASS FLUX (lbm/s/ft2) BREAK AREA (ft2)
VESSEL SIDE:
0.00255 21200 0.0316 0.00496 21200 0.0964 0.00737 21200 0.1892 0.01180 21200 0.4548 0.01580 21200 0.7631 0.02080 21200 1.0843 0.02081 8410 1.3317 0.02180 8410 1.4346 0.02380 8410 1.6361 0.02780 8410 2.0142 0.03580 8410 2.6280 0.03700 8410 2.7333 0.41400 8410 3.6440 0.41410 8410 3.6440 1.0 8410 3.6440 PUMP SIDE:
0.00255 21200 0.0316 0.00496 21200 0.0964 0.00737 21200 0.1892 0.01180 21200 0.4548 0.01580 21200 0.7631 0.02080 21200 1.0843 0.02081 8410 1.3317 0.02180 8410 1.4346 0.02380 8410 1.6361 0.02780 8410 2.0142 0.03580 8410 2.6290 0.03700 8410 2.7333 0.41400 8410 1.8220 0.41410 8410 0.4420 1.0 8410 0.4420 NOTE: The information presented in this table is based on original plant conditions. The values in the table do provide a reasonable representation of the general blowdown characteristics.
APPENDIX 6A 6A-7 REV. 13, SEPTEMBER 2006
(1)
Listed below are pertinent physical parameters used in the blowdown estimation:
A = 3.644 ft2 Minimum cross-sectional area between vessel and break D = 2.154 ft Pipe I.D. at the break location ho = 527.85 Btu/lbm Vessel enthalpy LI = 2.917 ft Inventory length Po = 1031.2 psia Vessel pressure Psat = 908 psia Saturation pressure
= 0.02127 ft3/lbm Specific volume of the fluid initially in the pipe V = 135 ft3 Inventory volume (2)
The postulated break location is at the nozzle safe-end to the pipe weld, which is located about 4.5 inches from the drywell side of the shield wall. A double-ended guillotine break was assumed. This is conservative because there is insufficient clearance for complete separation of the pipe and nozzle.
NOTE: The information presented in this table is based on original plant conditions.
APPENDIX 6A 6A-8 REV. 13, SEPTEMBER 2006
LGS UFSAR Table 6A-3 REACTOR PRIMARY SYSTEM BLOWDOWN FLOW RATES AND FLUID ENTHALPY - FEEDWATER LINE BREAK TIME (s) MASS FLOW (lbm/s) ENTHALPY (Btu/lbm) 0.0 0 404.5 0.0001 20348 404.5 0.0217 20348 404.5 0.0218 18454 404.5 1.0 18454 404.5 NOTE: The information presented in this table is based on original plant conditions. The values in the table do provide a reasonable representation of the general blowdown characteristics.
APPENDIX 6A 6A-9 REV. 13, SEPTEMBER 2006
LGS UFSAR Table 6A-4 FEEDWATER LINE BREAK BLOWDOWN MASS FLUX TIME HISTORY(1)
EFFECTIVE 2
TIME (s) MASS FLUX (lbm/s/ft ) BREAK AREA (ft2)
VESSEL SIDE:
0.0001 18250 0.3717 0.0217 18250 0.3717 0.0218 18250 0.2679 1.0 18250 0.2679 (2)
SUPPLY PIPE SIDE 0.0001 18250 0.7433 1.0 18250 0.7433 (1)
Listed below are some pertinent physical parameters used in the blowdown estimation A = 0.7433 ft2 Minimum cross-sectional area between vessel and break D = 0.9728 ft Pipe I.D. at the break location ho = 404.5 Btu/lbm Vessel enthalpy LI = 12 ft Inventory length Po = 1053 psia Vessel pressure Psat = 326 psia Saturation pressure
= 0.01888 ft3/lbm Specific volume of the feedwater V = 2.79 ft3 Inventory volume (1)
The most restricted flow area on the feedwater supply pipe side is the break area itself.
Full break area steady-state blowdown from this side is conservatively assumed to be reached immediately after the pipe rupture.
NOTE: The information presented in this table is based on original plant conditions. The values in the table do provide a reasonably represent the general characteristics of the blowdown mass flux time history.
APPENDIX 6A 6A-10 REV. 13, SEPTEMBER 2006
LGS UFSAR Table 6A-5 HEAD SPRAY LINE BREAK(1)(2)
TIME STEAM FLOW STEAM ENTHALPY (s) lbm/s) (Btu/lb) 0.0 506.8 1192 20.0 506.8 1192 (1)
Head spray line break is based on 6 inch Schedule 80 pipe with Moody Blowdown corresponding to 2800 lbm/sec-ft2. Overall containment response is that of a "small break accident."
(2)
This table is based on the original design basis power. the effects of rerate power conditions blowdown are shown in Figure 6A-11.
APPENDIX 6A 6A-11 REV. 13, SEPTEMBER 2006
LGS UFSAR Table 6A-6 COMPARTMENT VOLUMES USED IN REACTOR VESSEL SHIELD ANNULUS SUBCOMPARTMENT ANALYSIS COMPARTMENT NO. DESIGNATION VOLUME, ft3 1 V1 54 2 V2 54 3 V3 54 4 V4 54 5 V5 54 6 V6 54 7 V7 54 8 V8 54 9 V9 54 10 V10 54 11 V11 54 12 V12 54 13 V13 69 14 V14 76 15 V15 75 16 V16 76 17 V17 76 18 V18 69 19 V19 69 20 V20 76 21 V21 75 22 V22 76 23 V23 76 24 V24 69 25 V25 59 26 V26 57 27 V27 57 28 V28 57 29 V29 57 30 V30 57 31 V31 57 32 V32 57 33 V33 57 34 V34 57 35 V35 57 36 V36 59 37 V37 60 38 V38 58 39 V39 60 40 V40 76 41 V41 58 APPENDIX 6A 6A-12 REV. 13, SEPTEMBER 2006
COMPARTMENT NO. DESIGNATION VOLUME, ft3 42 V42 60 43 V43 76 44 V44 58 45 V45 60 46 V46 76 47 V47 58 48 V48 60 49 V49 77 50 V50 71 51 V51 73 52 V52 77 53 V53 75 54 V54 77 55 V55 77 56 V56 74 57 V57 77 58 V58 73 59 V59 71 60 V60 77 61 V61 34 62 V62 34 63 V63 34 64 V64 34 65 V65 34 66 V66 34 67 V67 34 68 V68 34 69 V69 34 70 V70 34 71 V71 34 72 V72 34 73 V73 235200 APPENDIX 6A 6A-13 REV. 13, SEPTEMBER 2006
LGS UFSAR Table 6A-7 FLOW AREA AND COEFFICIENTS USED IN REACTOR VESSEL SHIELD ANNULUS SUBCOMPARTMENT ANALYSIS FLOW FLOW AREA K L/A FLOW PATHS (ft2) FACTOR DESCRIPTION (ft-1) COEFFICIENT 1-2,1-12, 2-3,3-4, 4-5,5-6, 6-7,7-8, 8-9,9-10, 0.13 30o turn 10-11,11-12 10 1.0 Final expansion 0.62 0.94 1-13,2-14, 3-15,4-16, 5-17,6-18, 7-19,8-20, 9-21,10-22, 0.05 Friction 11-23,12-24 8.5 1.0 Final expansion 1.01 0.97 2-73,3-73, 5-73,6-73, 8-73,9-73, 0.42 Contraction 11-73,12-73 2 1.0 Final expansion 0.73 0.83 0.13 30o turn 13-24, 1.12 Around pipe 18-19 9.5 1.0 Final expansion 0.54 0.66 13-14,15-16, 16-17,17-18, 0.13 30o turn 19-20,20-21, 0.1 Around pipe 22-23,23-24 13 1.0 Final expansion 0.43 0.9 0.1 Around pipe 0.1 Around instrument pipe 14-15, 0.13 30o turn 21-22 12 1.0 Final expansion 0.43 0.86 1.35 Around pipe 13-25,18-30, 0.28 Around pipe 19-31,24-36 4.5 1.0 Final expansion 1.57 0.61 14-26,16-28, 0.28 Around pipe 17-29,20-32, 0.28 Around pipe 22-34,23-35, 5.5 1.0 Final expansion 1.17 0.8 APPENDIX 6A 6A-14 REV. 13, SEPTEMBER 2006
FLOW FLOW AREA K L/A FLOW PATHS (ft2) FACTOR DESCRIPTION (ft-1) COEFFICIENT 0.28 Around pipe 0.28 Around pipe 15-27, 0.31 Around pipe 21-33 4.5 1.0 Final expansion 1.31 0.73 25-36, 0.13 30o turn 30-31 11 1.0 Final expansion 0.55 0.94 25-26,26-27, 27-28,28-29, 29-30,31-32, 0.13 30o turn 32-33,33-34, 0.16 Around pipe 34-35,35-36, 9.5 1.0 Final expansion 0.58 0.88 25-37,26-38, 27-39,28-40, 29-41,30-42, 31-43,32-44, 33-45,34-46, 0.07 Friction 33-47,36-48 8.5 1.0 Final expansion 0.92 0.96 0.13 30o turn 37-48,38-39 0.01 Around instrument pipe 41-42,45-46 10.5 1.0 Final expansion 0.55 0.93 0.13 30o turn 37-38,40-41, 0.16 Around pipe 44-45,47-48 9.5 1.0 Final expansion 0.57 0.88 39-40,42-43, 0.13 30o turn 43-44,46-47 11 1.0 Final expansion 0.55 0.94 0.01 Around instrument pipe 37-49, 0.07 Friction 48-60 8 1.0 Final expansion 1.07 0.96 38-50,41-53, 1.11 Around pipe 44-56,47-59 6 1.0 Final expansion 1.14 0.68 39-51,42-54, 0.08 Around instrument pipe 45-57 8 1.0 Final expansion 1.07 0.96 APPENDIX 6A 6A-15 REV. 13, SEPTEMBER 2006
FLOW FLOW AREA K L/A FLOW PATHS (ft2) FACTOR DESCRIPTION (ft-1) COEFFICIENT 40-52,43-55 0.07 Around pipe 46-58 8.5 1.0 Final expansion 1.06 0.96 o
0.13 30 turn 0.15 Around pipe 49-50 0.15 Around pipe 59-60 11.5 1.0 Final expansion 0.46 0.83 o
0.125 30 turn 0.01 Around instrument pipe 49-60 14 1.0 Final expansion 0.42 0.93 0.13 30o turn 0.01 Around instrument pipe 0.47 Around pipe 50-51 10.5 1.0 Final expansion 0.48 0.78 0.13 30o turn 51-52,52-53, 0.15 Around pipe 56-57 13 1.0 Final expansion 0.44 0.88 0.13 30o turn 0.01 Around instrument pipe 0.15 Around pipe 53-54,57-58 12.5 1.0 Final expansion 0.45 0.88 0.13 30o turn 54-55 14.5 1.0 Final expansion 0.42 0.94 0.13 30o turn 0.15 Around pipe 0.12 Around CRD 0.15 Around pipe 55-56 10.5 1.0 Final expansion 0.5 0.8 o
0.13 30 turn 0.47 Around pipe 58-59 11 1.0 Final expansion 0.47 0.79 49-61,52-64, 53-65,55-67, 0.49 Around pipe 57-69 6.5 1.0 Final expansion 0.96 0.81 APPENDIX 6A 6A-16 REV. 13, SEPTEMBER 2006
FLOW FLOW AREA K L/A FLOW PATHS (ft2) FACTOR DESCRIPTION (ft-1) COEFFICIENT 0.49 Around pipe 54-66, 0.08 Around instrument pipe 60-72 6 1.0 Final expansion 1.0 0.79 0.49 Around pipe 0.17 Around CRD 56-68 5.5 1.0 Final expansion 1.07 0.77 o
0.11 30 turn 61-62,63-64 0.96 Around pipe 67-68,69-70 5 1.0 Final expansion 1.03 0.69 61-72,62-63 o
64-65,66-67 0.11 30 turn 68-69,70-71 6.5 1.0 Final expansion 0.9 0.94 o
0.11 30 turn 0.96 Around pipe 65-66, 0.1 Around instrument pipe 71-72 4.5 1.0 Final expansion 1.1 0.67 61-73,63-73 64-73,66-73 67-73,69-73 0.12 Contraction 70-73,72-73 6 1.0 Final expansion 0.28 0.94 62-73,65-73 0.05 Contraction 68-73,71-73 7.5 1.0 Final expansion 0.28 0.97 0.49 Around pipe 50-62,51-63, 0.49 Around pipe 58-70,59-71 5 1.0 Final expansion 1.28 0.71 APPENDIX 6A 6A-17 REV. 13, SEPTEMBER 2006