ML18022A165
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BFN-26 3.7 Thermal and Hydraulic Design 3.7.1 Power Generation Objective The objective of the thermal and hydraulic design of the core is to achieve power operation of the fuel over the life of the core without sustaining fuel damage.
3.7.2 Power Generation Design Basis The thermal hydraulic design of the core shall provide the following characteristics:
- a. The ability to achieve rated core power output throughout the design lifetime of the fuel without sustaining fuel damage.
- b. The flexibility to adjust core power output over the range of plant load and load maneuvering requirements without sustaining fuel damage.
3.7.3 Safety Design Basis
- 1. The thermal hydraulic design of the core shall establish limits for use in setting devices of the nuclear safety systems so that no fuel damage occurs as a result of abnormal operational transients (see Chapter 14, Plant Safety Analysis).
- 2. The thermal hydraulic design of the core shall establish a thermal hydraulic safety limit for use in evaluating the safety margin relating the consequences of fuel barrier failure to public safety.
3.7.4 Thermal and Hydraulic Limits 3.7.4.1 Requirements for Steady-State Conditions For purposes of maintaining adequate fuel performance margin during normal steady-state operation, the Minimum Critical Power Ratio (MCPR) must not be less than the required MCPR operating limit, the Average Planar Linear Heat Generation Rate (APLHGR) must be maintained below the required Maximum APLHGR limit (MAPLHGR) and the Linear Heat Generation Rate (LHGR) must be maintained below the required Maximum LHGR limit (MLHGR). The steady-state MCPR, MAPLHGR, and MLHGR limits are determined by analysis of the most severe moderate frequency Abnormal Operational Transients (AOTs) to accommodate uncertainties and provide reasonable assurance that no fuel damage results during moderate frequency AOTs at any time in life.
3.7-1
BFN-26 3.7.4.2 Requirements for Abnormal Operational Transients (AOTs)
The MCPR, MAPLHGR, and MLHGR limits are established such that no safety limit is expected to be exceeded during the most severe moderate frequency AOT event as defined in Chapter 14, Plant Safety Analysis.
3.7.4.3 Summary of Design Bases In summary, the steady-state operating limits have been established to assure that the design bases are satisfied for the most severe moderate frequency AOT.
Demonstration that the steady-state MCPR, MAPLHGR, and MLHGR limits are not exceeded is sufficient to conclude that the design bases are satisfied.
3.7.5 Description of Thermal - Hydraulic Design of the Reactor Core 3.7.5.1 Critical Power Ratio A description of the critical power ratio is provided in Subsection 3.7.7.1, Critical Power. Criteria used to calculate the critical power ratio safety limit are given in GESTAR II (General Electric Standard Application for Reactor Fuel) (Reference 1) for GE reload fuel analyses and References 32 and 42 for AREVA reload analyses.
3.7.5.2 Average Planar Linear Heat Generation Rate (APLHGR)
Models used to calculate the APLHGR limit are given in Subsection 3.2.5.1, Evaluation Methods, as pertaining to the fuel mechanical design limits, and in Subsection 6.5.2.1, Analysis Model, as pertaining to 10 CFR 50, Appendix K limits.
3.7.5.3 Core Coolant Flow Distribution and Orificing Pattern The flow distribution to the fuel assemblies and bypass flow paths is calculated on the assumption that the pressure drop across all fuel assemblies and bypass flow paths is the same. This assumption has been confirmed by measuring the flow distribution in boiling water reactors (References 2, 3, and 4). The components of bundle pressure drop considered are friction, local, elevation, and acceleration (Subsections 3.7.5.4.1 through 3.7.5.4.4, respectively). Pressure drop measurements made in operating reactors confirm that the total measured core pressure drop and calculated core pressure drop are in good agreement. There is reasonable assurance, therefore, that the calculated flow distribution throughout the core is in close agreement with the actual flow distribution of an operating reactor.
An iteration is performed on flow through each flow path (fuel assemblies and bypass flow paths), which equates the total differential pressure (plenum to plenum) across each path and matches the sum of the flows through each path to the total core flow. The total core flow less the control rod cooling flow enters the lower 3.7-2
BFN-26 plenum. A fraction of this passes through various bypass flow paths. The remainder passes through the orifice in the fuel support plate (experiencing a pressure loss) where some of the flow exits through the fit-up between the fuel support and the lower tieplate and through the lower tieplate holes into the bypass flow region. All reload core fuel bundles have lower tieplate holes. The majority of the flow continues through the lower tieplate (experiencing a pressure loss) where some flow exits through the flow path defined by the fuel channel and lower tieplate into the bypass region. This bypass flow is lower for those fuel assemblies with finger springs. The bypass flow paths considered in the analysis and typical values of the fraction of bypass flow through each flow path are given in Reference 5.
Within the fuel assembly, heat balances on the active coolant are performed nodally.
Fluid properties are expressed as the bundle average at the particular node of interest. In evaluating fluid properties a constant pressure model is used.
For core design and monitoring, assembly-specific relative radial and axial power distributions are used with the bundle flow to determine the axial coolant property distribution, which gives sufficient information to calculate the pressure drop components within each fuel assembly type. When the equal pressure drop criterion described above is satisfied, the flow distributions are established.
3.7.5.4 Core Pressure Drop and Hydraulic Loads The components of bundle pressure drop considered are friction, local, elevation, and acceleration pressure drops. Pressure drop measurements made in operating reactors confirm that the total measured core pressure drop and calculated core pressure drop are in good agreement.
3.7.5.4.1 Friction Pressure Drop Friction pressure drop is calculated with a basic model as follows:
w2 fL 2 Pf = 2 TPF 2 gc DH Ach where 3.7-3
BFN-26 P f = friction pressure drop, psi w = mass flow rate g c = conversion factor
= average nodal liquid density DH = channel hydraulic diameter Ach = channel flow area L = incremental length f = friction factor TPF = two-phase friction multiplier The formulation for the two-phase multiplier for GE reload analyses is similar to that presented in References 7 and 8 based on data that is taken from proto-typical BWR fuel bundles. AREVA pressure drop methodology is described in References 33, 34, and 35.
3.7.5.4.2 Local Pressure Drop The local pressure drop is defined as the irreversible pressure loss associated with an area change, such as the orifice, lower tieplate, and spacers of a fuel assembly.
The general local pressure drop model is similar to the friction pressure drop and is w2 K 2 PL =
2 gc A 2 TPL where PL = local pressure drop, psi K = local pressure drop loss coefficient A = reference area for local loss coefficient TPL = two-phase local multiplier 3.7-4
BFN-26 and w, g, and are defined above. For GE reload analyses, the formulation for the two-phase multiplier is similar to that reported in Reference 8. For AREVA analyses the Reference 33, 34, and 35 methodologies are used. For advanced spacer designs a quality modifier has been incorporated in the two-phase multiplier to better fit the data. Empirical constants were added to fit the results to data taken for the specific designs of the BWR fuel assembly. These data were obtained from tests performed in single-phase water to calibrate the orifice, the lower tieplate, and the holes in the lower tieplate, and in both single-and two-phase flow, to derive the best fit design values for spacer and upper tieplate pressure drop. The range of test variables was specified to include the range of interest for boiling water reactors. New test data are obtained whenever there is a significant design change to ensure the most applicable methods are used.
3.7.5.4.3 Elevation Pressure Drop The elevation pressure drop is based on the relation:
g PE = L ;
gc
= f (1 ) + g where PE = elevation pressure drop, psi L = incremental length
= average mixture density g = acceleration of gravity
= nodal average void fraction f , g = saturated water and vapor density, respectively For GE reload analyses, the void fraction model used is an extension of the Zuber-Findlay model (Reference 9), and uses an empirically fit constant to predict a large block of steam void fraction data. AREVA void fraction models are described in References 33, 34, and 35.
3.7-5
BFN-26 3.7.5.4.4 Acceleration Pressure Drop A reversible pressure change occurs when an area change is encountered, and an irreversible loss occurs when the fluid is accelerated through the boiling process. The basic formulation for the reversible pressure change resulting from a flow area change in the case of single-phase flow is given by:
w2 PACC = (1 ) 2 A
2 gc f A22 A2 A =
A1 where PACC = acceleration pressure drop A2 = final flow area A1 = initial flow area In the case of two-phase flow, the liquid density is replaced by a density ratio so that the reversible pressure change is given by:
w 2 H PACC = (1 )2 A
2 gcKE2 A22 where 1 x (1 x )
= + , homogeneous density H g f 1 x3 (1 x ) 3 2 = 2 2+ 2 , kinetic energy density KE g f (1 )2
= void fraction at A2 x = steam quality at A2 and other terms are as previously defined. The basic formulation for the acceleration pressure change due to density change is:
3.7-6
BFN-26 w2 1 1 PACC = 2 gcAch OUT IN where is either the homogeneous density, H , or the momentum density, M 1 x2 (1 x )2
= +
M g f ( 1 )
and is evaluated at the inlet and outlet of each axial node. Other terms are as previously defined. The total acceleration pressure drop in boiling water reactors is on the order of a few percent of the total pressure drop.
3.7.5.5 Correlation and Physical Data General Electric Company and AREVA have obtained substantial amounts of physical data in support of the pressure drop and thermal-hydraulic loads discussed in Subsection 3.7.5.4, Core Pressure Drop and Hydraulic Loads. Correlations have been developed to fit these data to the formulations discussed.
3.7.5.5.1 Pressure Drop Correlations General Electric Company and AREVA have taken significant amounts of friction pressure drop data in multi-rod geometries representative of BWR plant fuel bundles and correlated both the friction factor and two-phase multipliers on a best fit basis using the pressure drop formulations reported in Subsections 3.7.5.4.1 and 3.7.5.4.2. Tests are performed in single-phase water to calibrate the orifice and the lower tie-plate, and in both single-phase and two-phase flow to arrive at best fit design values for spacer and upper tie-plate pressure drop. The range of test variables is specified to include the range of interest to boiling water reactors. New data are taken whenever there is a significant design change to ensure the most applicable methods are in use at all times.
Applicability of the single-phase and two-phase hydraulic models discussed in Subsections 3.7.5.4.1 and 3.7.5.4.2 have been confirmed by full scale prototype flow testing.
3.7.5.5.2 Void Fraction Correlation The void fraction correlation includes effects of pressure, flow direction, mass velocity, quality, and subcooled boiling.
3.7.5.5.3 Heat Transfer Correlation 3.7-7
BFN-26 For GE reload analyses, the Jens-Lottes (Reference 11) heat transfer correlation is used in fuel design to determine the cladding-to-coolant heat transfer coefficients for nucleate boiling. The fuel heat transfer correlations for AREVA reload analyses are described in Reference 37.
3.7.5.6 Thermal Effects of Abnormal Operational Transients The evaluation of the cores capability to withstand the thermal effects resulting from abnormal operational transients is covered in Chapter 14, Plant Safety Analysis.
3.7.5.7 Uncertainties in Estimates Uncertainties in thermal-hydraulic parameters are considered in the statistical analysis which is performed to establish the fuel cladding integrity safety limit documented in Subsection 3.7.7.1.1, Fuel Cladding Integrity Safety Limit.
3.7.5.8 Flux Tilt Considerations For flux tilt considerations, refer to Subsection 3.6.4.2, Power Distribution.
3.7.6 Description of the Thermal-Hydraulic Design of the Reactor Coolant System 3.7.6.1 Power/Flow Operating Map 3.7.6.1.1 Performance Range for Normal Operations A boiling water reactor must operate within certain restrictions due to pump net positive suction head (NPSH) requirements, overall plant control characteristics, core thermal power limits, etc. Operating power-flow maps for BFN Units 1, 2, and 3 are shown in Figures 3.7-1, 3.7-2, and 3.7-3, respectively. The nuclear system equipment, nuclear instrumentation, and the Reactor Protection System, in conjunction with operating procedures, maintain operations within the shaded area of the maps for normal operating conditions. The boundaries on the maps are as follows:
Natural Circulation Line The operating state of the reactor moves along this line for the normal control rod withdrawal sequence in the absence of recirculation pump operation.
20 Percent Pump Speed Line The operating state for the reactor follows this line for the normal control rod withdrawal sequence with recirculation pumps operating at approximately 20 percent speed.
3.7-8
BFN-26 Design Flow Control Line The design flow control line passes through 100 percent power at 100 percent flow.
The operating state for the reactor follows this line (or one parallel to it) for recirculation flow changes with a fixed control rod pattern. The line is based on constant xenon concentration.
APRM Rod Block Line The line shown on the graph limits control rod withdrawal to within the constraint of the control rod block line.
Pump Constant Speed Line This line shows the change in flow associated with power reduction from 100 percent power, 100 percent flow, while maintaining constant recirculation pump speed.
Minimum Expected Flow Control Line This line represents the flow control line for plant startup in which the recirculation pump speed is increased above 20 percent speed before control rod withdrawal is continued.
Increased Core Flow (ICF) Region The plant is licensed for Increased Core Flow (ICF) operation up to a maximum of 105% of rated core flow at 100% rated power. At core thermal powers less than rated, the maximum allowable core flow is set by the constant recirculation pump speed line that passes through the 100% power and 105% flow point on the Power/Flow operating map. ICF can be used to extend full power operation beyond the point where all rods are out at rated power and flow conditions (End Of Full Power Life - EOFPL). ICF may be used prior to reaching EOFPL for operating flexibility.
Maximum Extended Load Line Limit Analysis (MELLLA) Region The plant is licensed for Maximum Extended Load Line Limit Analysis (MELLLA) which allows operation at full power down to 75% rated flow conditions. (Note: with power uprate, MELLLA allows operation at full power down to 81% rated flow conditions.) The MELLLA region may be used to set target rod patterns on a higher rod line to accommodate xenon accumulation. The MELLLA region also increases the allowance for flow window operation such as compensating for small core 3.7-9
BFN-26 reactivity changes with burnup by adjusting core flow. This reduces the need to continually adjust rod patterns.
3.7.6.1.2 Flow Control The following simple description of boiling water reactor operation with recirculation flow control summarizes the principal modes of normal power range operation.
Assuming the plant to be initially hot with the reactor critical, full power operation can be approached following the sequence shown as points 1 to 7 in Figure 3.7-1. The first part of the sequence (1 to 3) is achieved with control rod withdrawal and manual, individual recirculation pump control. Individual pump startup procedures are provided which achieve 28 percent of full pump speed in each loop. The natural circulation characteristics of the boiling water reactor are still influential at this pump speed level as shown in the appropriate curve. Power, steam flow, and feedwater flow are increased as control rods are manually withdrawn until the feedwater flow has reached approximately 20 percent. An interlock on feedwater flow prevents low power-high recirculation flow combinations which may create recirculation pump NPSH problems.
Once the feedwater interlock is cleared, the operator can manually increase recirculation flow in each loop until the operating state reaches point 3.
The recirculation system master controller is limited, and these limits establish the operating state (see Subsection 7.9, Recirculation Flow Control System). An example power flow map is shown in Figure 3.7-1.
Reactor power increases as the operating state moves from point 2 to 3 due to the inherent flow control characteristics of the boiling water reactor. At point 3 the operator may switch to Master Manual recirculation pump control. Thermal output can then be increased by either control rod withdrawal or recirculation flow increase.
For example, the operator can reach approximately 40 percent power in the ways indicated by points 4 and 5. With an increase of recirculation pump speed, point 4 can be achieved.
The curves labeled Minimum Expected Flow Control Line and Design Flow Control Line represent typical steady-state power-flow characteristics for fixed rod patterns. They are slightly affected by xenon, differences in core leakage flow assumptions, and reactor vessel pressure variations. However, for this example, these effects have been neglected.
Normal power range operation is along or parallel to the Design Flow Control Line.
If load following response is desired in either direction, plant operation near 90 percent power provides the most capability. If maximum load pickup capability is desired, the nuclear system can be operated near point 6, with fast load response available all the way up to rated power near point 7.
3.7-10
BFN-26 The large negative operating coefficients, which are inherent in the boiling water reactor, provide important advantages as follows:
- a. Good load following with well damped behavior and little undershoot or overshoot in the heat transfer response.
- b. Load following with recirculation flow control.
- c. Strong damping of spatial power disturbances.
Load following is accomplished by manually varying the recirculation flow to the reactor. This method of power level control takes advantage of the reactor negative void coefficient. To increase reactor power, it is necessary only to increase the recirculation flow rate which sweeps some of the voids from the moderator, causing an increase in core reactivity. As the reactor power increases, more steam is formed and the reactor stabilizes at a new power level with the transient excess reactivity balanced by the new void formation. No control rods are moved to accomplish this power level change. Conversely, when a power reduction is required, it is necessary only to reduce the recirculation flow rate. When this is done, more voids are formed in the moderator, and the reactor power output automatically decreases to a new power level commensurate with the new recirculation flow rate. No control rods are moved to accomplish the power reduction.
Load following through the use of variations in the recirculation flow rate (flow control) is advantageous relative to load following by control rod positioning. Flow variations perturb the reactor uniformly in the horizontal planes, and thus allow operation with flatter power distribution and reduced transient allowances. As the flow is varied, the power and void distributions remain approximately constant at the steady-state end points for a wide range of flow variations. These constant distributions provide the important advantage that the operator can adjust the power distribution at a reduced power and flow by movement of control rods and then bring the reactor to rated conditions by increasing flow, with the assurance that the power distribution will remain approximately constant. Subsection 7.9, Recirculation Flow Control System, describes the means by which recirculation flow is varied.
3.7.6.2 Thermal-Hydraulic Stability Performance The GE analytical methodology for demonstrating stability compliance for GE fuel designs on a generic basis is described in Subsection 3.6.4.6, Stability. To provide additional assurance that regional instabilities will not occur, Browns Ferry has implemented the long-term stability solution designated as Option III in NEDO-31960, Supplement 1, BWR Owners Group Long-Term Stability Solution Licensing Methodology.
3.7-11
BFN-26 For the Option III long-term stability solution, the Oscillation Power Range Monitor (OPRM) Upscale Trip function of the Power Range Neutron Monitoring (PRNM) system is enabled. [Note: See Section 7.5.7.3.5 for a detailed description of the OPRM system.] The OPRM Upscale Trip function provides protection from exceeding the fuel MCPR Safety Limit in the event of thermal-hydraulic power oscillations. The OPRM receives input signals from the Local Power Range Monitors (LPRMs) within the reactor core. An Upscale Trip is issued if oscillatory changes in the neutron flux are detected. The OPRM Upscale Trip function is required to be operable when the plant is in a region of power-flow operation where actual thermal-hydraulic oscillations might occur (Tech Spec enabled region -
greater than 25% rated thermal power and less than 60% recirculation drive flow).
Power/flow maps for BFN Units 1, 2, and 3 indicating the OPRM auto enable region are shown in Figures 3.7-1, 3.7-2, and 3.7-3, respectively.
A cycle specific Option III stability analysis is performed for each reload core to determine the appropriate OPRM setpoint. The analysis considers both steady state startup operation and the case of a two recirculation pump trip from rated power.
The resulting stability based Operating Limit MCPRs as a function of OPRM setpoint are reported in the GE Supplemental Reload Licensing Report or AREVA Reload Analysis Report (included in Appendix N of the FSAR). The actual OPRM setpoint is selected such that required margin to the MCPR Safety Limit is provided without stability being a limiting event.
If the OPRM trip function should become inoperable, alternate methods to detect and suppress oscillations may be implemented in accordance with the Technical Specifications.
3.7.7 Evaluation The thermal-hydraulic design of the reactor core and reactor coolant system is based upon an objective of no fuel damage during normal operation or during abnormal operational transients. This design objective is demonstrated by analysis as described in the following sections.
3.7.7.1 Critical Power The objective for normal operation and AOTs is to maintain nucleate boiling and thus avoid a transition to film boiling. Operating limits are specified to maintain adequate margin to the onset of the boiling transition. The figure of merit utilized for plant operation is the critical power ratio (CPR). This is defined as the ratio of the critical power (bundle power at which some point within the assembly experiences onset of boiling transition) to the operating bundle power. The critical power is determined at the same mass flux, inlet temperature, and pressure which exists at the specified reactor condition. Thermal margin is stated in terms of the minimum value of the critical power ratio (MCPR), which corresponds to the most limiting fuel 3.7-12
BFN-26 assembly in the core. To ensure that adequate margin is maintained, a design requirement based on a statistical analysis was selected as follows:
Moderate frequency AOTs caused by a single operator error or equipment malfunction shall be limited such that, considering uncertainties in manufacturing and monitoring the core operating state, at least 99.9% of the fuel rods would be expected to avoid boiling transition (Reference 13).
Both the transient (safety) and normal operating thermal limits in terms of MCPR are derived from this basis.
3.7.7.1.1 Fuel Cladding Integrity Safety Limit The generation of the Minimum Critical Power Ratio (MCPR) limit requires a statistical analysis of each reload core near the limiting MCPR condition. The MCPR Fuel Cladding Integrity Safety Limit applies not only for core wide AOTs, but is also applied to the localized rod withdrawal error AOT. The cycle-specific Safety Limit MCPR is derived based on methodology documented in GESTAR II (Reference 1) for GE reload analyses, and References 32 and 42 for AREVA reload analyses. For AREVA reload analyses, the Reference 43, 44, and 46-47 approved critical power correlations are used as appropriate to specific fuel types.
The resulting safety limit MCPR for each cycle is given in the GE Supplemental Reload Licensing Report (SRLR) or AREVA Reload Analysis Report for each BFN unit (included in Appendix N of the FSAR).
Statistical Model The statistical analysis utilizes a model of the BWR core which simulates the process computer function. This code produces a critical power ratio (CPR) map of the core based on inputs of power distribution, flow, and heat balance information.
Details of the procedure are documented in Appendix IV of Reference 13 and Section 4 of Reference 14 for GE reload analyses and References 32 and 42 for AREVA reload analyses. Random Monte Carlo selections of all operating parameters based on the uncertainty ranges of manufacturing tolerances, uncertainties in measurement of core operating parameters, calculational uncertainties, and statistical uncertainty associated with the critical power correlations are imposed upon the analytical representation of the core and the resulting bundle critical power ratios are calculated. Uncertainties used in the cycle-specific statistical analysis are presented in References 10, 14, and 15 for GE reload analyses; uncertainties typical of AREVA cycle-specific analyses are provided in Reference 39.
3.7-13
BFN-26 The minimum allowable critical power ratio is set to correspond to the criterion that 99.9% of the rods are expected to avoid boiling transition by interpolation among the means of the distributions formed by all the trials.
BWR Statistical Analysis Statistical analyses are performed for each operating cycle that provide the fuel cladding integrity safety limit MCPR. This safety limit MCPR is derived based on methodology documented in Reference 42.
3.7.7.1.2 MCPR Operating Limit Calculational Procedure A plant-unique MCPR operating limit is established to provide adequate assurance that the cycle-specific fuel cladding integrity safety limit for the plant is not exceeded for any moderate frequency AOT. This operating requirement is obtained by addition of the maximum CPR value for the most limiting AOT (including any imposed adjustment factors) from conditions postulated to occur at the plant to the cycle-specific fuel cladding integrity safety limit.
Calculational Procedure for AOT Pressurization Events Core-wide rapid pressurization events (turbine trip w/o bypass, load rejection w/o bypass, feedwater controller failure) are analyzed using the system model (ODYN) documented in References 16 and 17 for GE reload analyses and COTRANSA2 (Reference 40) for AREVA reload analyses. An updated version of ODYN using the advanced physics methods of Reference 18 as described in Reference 19 is used for GE reload analyses.
For GE11 and later fuel products the Time Varying Axial Power Shape (TVAPS) is calculated by ODYN (Reference 20) for GE reload analyses. The TVAPS calculation is performed by COTRANSA2 (Reference 40) for AREVA reload analyses. The TVAPS is a short time period phenomena that occurs during the control rod scram that terminates an AOT. The analytical procedures used to evaluate the AOTs account for TVAPS either in a bounding manner or explicitly, depending on the AOT and the fuel design.
Calculational Procedure for AOT Slow Events The slower core-wide abnormal operational transient, loss of feedwater heating (LFWH), is analyzed using either the steady-state 3-D BWR Simulator Code (References 18 and 45), or the REDY transient model (References 21, 22, and 23) as described in Reference 24 for GE reload analyses. For AREVA reload analyses, the MICROBURN-B2 (Reference 35) 3-D simulator code is used for quasi-steady-state LFWH transients; for transient events that cannot be handled in a quasi-3.7-14
BFN-26 steady-state manner, the COTRANSA2 (Reference 40) is used. Inadvertent HPCI startup is not analyzed when the core enthalpy change is bounded by that of the loss of feedwater heating event (Reference 25). When necessary, it is analyzed using the REDY transient model for GE reload analyses or COTRANSA2 for AREVA analyses. The scram reactivity used for slow events is documented in GESTAR II (Reference 1) for GE analyses.
Rod Withdrawal Error Calculational Procedure The reactor core behavior during the rod withdrawal error transient is calculated by doing a series of steady-state three-dimensional coupled nuclear-thermal-hydraulic calculations using the 3-D BWR Simulator (References 18 and 45) for GE reload analyses or Reference 35 for AREVA analyses).
Event Descriptions For GE reload analyses, descriptions of the limiting AOT events are given in the country-specific supplement to GESTAR II (Reference 6). The AOT descriptions given in Reference 6 are used as a basis for the typical analyses performed. Some plant-unique analyses will differ in certain aspects from the typical calculational procedure depending on which margin improvement options are selected.
For AREVA analyses, the AOT descriptions in Chapter 14 of this UFSAR are utilized with appropriate cycle-specific input parameter updates.
MCPR Operating Limit Calculation For GE reload analyses, the operating limit MCPR for rapid AOTs is calculated using the TASC computer program (Reference 26). The country-specific supplement to GESTAR II (Reference 6) lists the plant initial conditions for the MCPR operating limit analysis. Any different values used in the reload analyses to those given in Reference 6 are reported in the SRLR. Cycle-dependent plant initial conditions for the MCPR operating limit analysis and the resulting parameters are also given in the SRLR.
For AREVA reload analyses, the CPR for rapid AOTs is calculated using XCOBRA (Reference 41) for the initial steady-state analysis and XCOBRA-T (Reference 37) for the transient thermal margin analysis of the limiting fuel assembly.
MCPR Uncertainty Considerations for GE Reload Analyses The deterministic CPR value which results from ODYN/TASC evaluations (for all rapid pressurization AOTs) must be adjusted such that a 95/95 CPR/ICPR licensing basis is calculated (i.e., 95% probability with 95% confidence that the 3.7-15
BFN-26 safety limit will not be violated). The SER which describes these requirements and procedures is given in Reference 27.
The plant has the choice of operating under either Option A or Option B.
Option A - Under Option A, the MCPR for each event is determined using statistically evaluated scram times. If the plant does not demonstrate compliance with the statistically evaluated scram times, it must operate using a higher limit that does not take credit for these scram times. The higher limit is also referred to as Option A. Details are provided in Reference 27.
Option B - Under Option B, the CPR/ICPR ratio for the pressurization events is evaluated on either a plant-unique or generic statistical basis per the methodology and procedures of Reference 28. The generic basis utilizes adjustment factors which are dependent on plant and event type. The adjustment factors and their application are described in References 28 and 31. For operation under Option B, the plant must demonstrate that actual scram speeds are within the distribution assumed in the derivation of the adjustment factors. This conformance procedure is described in Reference 27.
The adjusted MCPR values for all rapid pressurization events are reported in the SRLR.
MCPR Uncertainty Considerations for AREVA Reload Analyses For fast transient events, the one-dimensional kinetic thermal-hydraulic COTRANSA2 code is used for the reactor system analysis, with the XCOBRA/XCOBRA-T codes evaluating the initial and transient hot channel hydraulics and CPR. The NRC approved application methodology of References 40, 41, and 42 provides adequate conservatism by accounting for uncertainties in the computed CPR results. Therefore, for a given transient event, the required operating limit MCPR (OLMCPR) is simply the XCOBRA-T calculated CPR added to the safety limit MCPR (SLMCPR).
The results of the system pressurization transients are sensitive to the control rod scram speed used in the calculations. To take advantage of average scram speeds faster than those associated with the technical specifications surveillance times, scram speed-dependent MCPR limits are provided. If the control rod scram time performance is equal or better than the nominal scram speed (NSS) insertion times specified in the core operating limits report (COLR), the NSS-based MCPR operating limits apply. If the control rod scram time performance is equal or better than the optimal scram speed (OSS) insertion times specified in the COLR, the 3.7-16
BFN-26 OSS-based MCPR operating limits apply. Otherwise, MCPR operating limits are applied that are based on the technical specification scram speed (TSSS) control rod insertion times. The plant technical specifications allow for operation with a certain number and arrangement of slow control rods as well as one stuck control rod. Conservative adjustments to the OSS, NSS, and TSSS scram speeds are input to the reload transient analyses to account for these slow and stuck rod effects on scram reactivity.
TSSS, NSS, and OSS-based power-dependent MCPR operating limits are reported in the reload licensing analysis report.
Low Flow and Low Power Effects on MCPR The operating limit MCPR must be increased for low flow and, for plants with ARTS, low power conditions. This is because, in the BWR, power increases as core flow increases which results in a corresponding lower MCPR. If the MCPR at a reduced flow condition were at the 100% power and flow MCPR operating limit, a sufficiently large inadvertent flow increase could cause the MCPR to decrease below the Fuel Cladding Integrity Safety Limit MCPR.
Plants licensed for the Average Power Range Monitor, Rod Block Monitor, and Technical Specification (ARTS) Improvement Program have both power- and flow-dependent limits imposed on the operating limit MCPR (OLMCPR). The flow-dependent required OLMCPR, MCPRf, is defined as a function of the core flow rate and maximum rated power core flow capability. For powers between 100% of rated and the bypass point for the turbine stop valve/turbine control valve fast closure scram signal (about 30% of rated), the power-dependent OLMCPR, MCPRp, is directly supplied (AREVA methods) or determined from the product of the OLMCPR at 100% of rated and a power-dependent multiplier, Kp (GE methods). For powers between 25% rated and the bypass point, the MCPRp limits are absolute values and are defined separately for high core flows (>50% of rated flow) and for low core flows (50% of rated flow) conditions. There is no thermal limits monitoring required below 25% of rated power. The OLMCPR to be used at powers less than 100%
becomes the most limiting value of either MCPRf or MCPRp.
End-of-Cycle Coastdown Considerations AOT analyses are performed at the full power, EOC, all-rods-out condition.
Once an individual plant reaches this condition, it may shutdown for refueling or it may be placed in a coastdown mode of operation. In the end-of-cycle coastdown type of operation the plant is allowed to coastdown to a lower percent of rated power while maintaining core flow at the constant pump speed line corresponding to rated core flow at rated core thermal power. The power during this 3.7-17
BFN-26 period is conservatively analyzed in a manner that overpredicts the power level for any given exposure.
For GE methods, in Reference 29, evaluations were made at 90%, 80%, and 70%
power level points on the linear curve. The results show that the pressure and MCPR from the limiting pressurization AOT exhibit a larger margin for each of these points than the EOC full power, full flow case. MLHGR limits for the full power, rated flow case are conservative for the coastdown period, since the power will be decreasing and rated core flow will be maintained. Therefore, it can be concluded that the coastdown operation beyond full power operation is conservatively bounded by the analysis at the EOC conditions. In Reference 30, this conclusion is confirmed for coastdown operation down to 40% power and is shown to hold for analyses performed with ODYN.
For AREVA methods, the nominal start of coastdown cycle exposure is conservatively extended. Coastdown limits are then determined at the final cycle exposure bounding of anticipated operation, forming the licensing basis maximum core average exposure (CAVEX).
3.7.7.2 Analysis Options 3.7.7.2.1 MCPR Margin Improvement Options Several MCPR margin improvement options have been developed for operating BWRs. The following options are utilized at Browns Ferry:
(1) Recirculation Pump Trip (2) Thermal Power Monitor (3) Exposure-Dependent Limits (4) Improved Scram Times The exposure-dependent limits option is used on an as-needed basis. The GE Supplemental Reload Licensing Report, or AREVA Reload Analysis Report, for each unit indicates which options are currently analyzed.
Recirculation Pump Trip For many of the plant operating cycles, the limiting AOTs are the turbine trip, generator load rejection, or other AOTs which result in a turbine trip. A significant improvement in thermal margin can be realized if the severity of these transients is reduced. The Recirculation Pump Trip (RPT) feature accomplishes this by cutting off power to the recirculation pump motors anytime that the turbine control valve or turbine stop valve fast closure occurs.
3.7-18
BFN-26 This rapid reduction in recirculation flow increases the core void content during the AOT, thereby reducing the peak AOT power and heat flux.
Basically, the RPT consists of switches installed in both the turbine control valves and the turbine stop valves. When these valves close, breakers are tripped which releases the recirculation pumps to coast down under their own inertia.
Thermal Power Monitor The APRM simulated thermal power trip (APRM thermal power monitor) is a minor modification to the APRM system. The modified APRM system generates two upscale trips. On one, the APRM signal (which is proportional to the thermal neutron flux) is compared with a reference which is not dependent on flow rate.
During normal reactor operations, neutron flux spikes may occur due to conditions such as transients in the recirculation system, transients during large flow control load maneuvers, or transients during turbine stop valve tests. The neutron flux leads the heat flux during transients because of the fuel time constant. And the neutron flux for these transients trips upscale before the heat flux increases significantly. (High heat flux is the precursor of fuel damage.) Thus, increased availability can be achieved without fuel jeopardy by adding a trip dependent on heat flux (thermal power).
For this trip, the APRM signal is passed through a low pass RC filter. It is compared with a recirculation flow rate dependent reference which decreases approximately parallel to the flow control lines.
In addition to increased availability, another benefit is that with the minor operational spikes filtered out, the heat flux trip setpoint is lower than the neutron flux trip setpoint. For long, slow AOTs such as the loss-of-feedwater heater, the heat flux and neutron flux are almost in equilibrium. For these AOTs, the lower trip setpoint results in an earlier scram with a smaller increase in heat flux and a corresponding reduction in the consequences.
The APRM Simulated Thermal Power Trip at Browns Ferry is non-safety grade and is not taken credit for in any of the licensing transient analyses.
Exposure-Dependent Limits The severity of any plant AOT pressurization event is worst at the end of the cycle primarily because the EOC all-rods-out scram curve gives the worst possible scram response. It follows that some limits relief may be obtained by analyzing the AOTs at other interim points in the cycle and administering the resulting limits on an exposure dependent basis.
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BFN-26 This technique is straightforward and consists merely of repeating certain elements of the AOT analyses for selected midcycle exposures. Because the scram reactivity function monotonically deteriorates with exposure (after the reactivity peak), the limit determined for an exposure Ei is administered for all exposures in the interval Ei-1 < E Ei where Ei-1 is the next lower exposure point for which a limit was determined. This results in a table of MCPR limits to be applied through different exposure intervals of the cycle.
Improved Scram Times For GE reload analyses, GE has developed a generic statistical scram time distribution for the purposes of generating the AOT CPR adjustment factors required for ODYN Option B (see Subsection 3.7.7.1.2, MCPR Operating Limit Calculational Procedure). By operating under Option B MCPR operating limits the plant is taking advantage of the improved scram time benefits on the AOT performance, by demonstrating that actual scram speeds conform with the generic statistical scram times assumed.
As described in Section 3.7.7.1.2, subsection titled MCPR Uncertainty Considerations for AREVA Reload Analyses, for AREVA reload analyses power-dependent MCPR limits are provided for OSS, NSS, and TSSS bases. OSS and NSS bases limits may be used depending on scram speed measurements.
Otherwise, the TSSS MCPR limits are applied. The TSSS and NSS-based power-dependent MCPR operating limits are reported in the reload licensing analysis report.
3.7.7.2.2 Operating Flexibility Options A number of operating flexibility options have been developed for BWRs. The following options are utilized at Browns Ferry:
(1) Load Line Limit (2) Extended Load Line Limit (3) Maximum Extended Load Line Limit (4) Increased Core Flow (5) Feedwater Temperature Reduction (6) Turbine Bypass Out of Service (7) ARTS Program (8) Recirculation Coolant Pump Out of Service (Single-Loop Operation)
(9) End-of-Cycle Recirculation Pump Trip Out of Service (10) Power Load Unbalance Out of Service 3.7-20
BFN-26 The GE Supplemental Reload Licensing Report (SRLR), or AREVA Reload Licensing Report for each unit indicates which options are currently analyzed (included in Appendix N of the FSAR).
Load Line Limit The capability to operate above the rated load line of the power-flow map offers the plant several definite operational advantages resulting in an increased overall plant capacity factor. The primary advantage is in the areas of plant startup with additional benefits in rated power operation and load-following assistance. By operating above the rated load line during power ascension, increasing xenon inventory can be countered with increases in core flow allowing rated power to be achieved without additional control rod adjustments.
During rated power operation, rated power conditions can be maintained for longer periods of time without control rod adjustments by using flow control to compensate for reactivity changes due to fuel depletion. An analysis referred to as the Load Line Limit Analysis (LLLA) is performed to determine if the safety consequences of operation above the rated load line, but within a defined region of the power flow map, are bounded by the respective consequences of operation at the licensing basis conditions.
The region above the rated load line is known as the extended operating region and is defined by the locus of power/flow points bounded by:
(1) the rated load line; (2) the APRM rod block line; and (3) the rod block intercept line and the rated power line.
LLLA is performed on a plant/cycle-specific basis. However, after the LLLA is initially performed for a plant and cycle, on subsequent cycles only the following checks need to be made in addition to the standard reload analyses to support operation in the extended operation region:
(1) LOCA - The applicability of previous LOCA analyses to the extended operating region must be verified each cycle.
(2) AOTs - The consequences of AOTs are evaluated to determine if operating limit adjustments are necessary for operation in the extended operating range.
Extended Load Line Limit The Extended Load Line Limit Analysis (ELLLA) is similar to the LLLA described above. However, the extended operating domain for ELLLA, instead, has an upper bound of the APRM rod block line to rated power.
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BFN-26 Once ELLLA has been performed for a specific plant and cycle, it is reverified for applicability to subsequent cycles as described in the LLLA discussion. Because of the different extended operating regions for ELLLA and LLLA, the power/flow points chosen for analysis may be different.
Maximum Extended Load Line Limit The Maximum Extended Load Line Limit Analysis (MELLLA) further expands the operating domain to allow operation at full power down to 75% rated flow conditions.
(Note: with power uprate, MELLLA allows operation at full power down to 81% rated flow conditions.) Addition of the MELLLA region provides improved power ascension capability to full power and additional flow range at rated power.
Evaluations performed for MELLLA conditions include normal and AOTs, LOCA analysis, containment responses, and stability. The reload fuel dependent results of these analyses are re-evaluated each cycle.
Increased Core Flow Operation Analyses are performed in order to justify operation at core flow rates in excess of the 100% rated flow condition. The limiting AOTs that are analyzed at rated flow as part of a standard supplemental reload licensing report are reanalyzed for increased core flow operation. In addition, the loss-of-coolant accident (LOCA), fuel loading error, rod drop accident, and rod withdrawal error are also re-evaluated for increased flow operation.
The effects of the increased pressure differences on the reactor internal components, fuel channels, and fuel bundles as a result of the increased flow are analyzed in order to ensure that the design limits will not be exceeded.
The thermal-hydraulic stability is re-evaluated for increased core flow operation, and the effects of flow-induced vibration are also evaluated to assure that the vibration criteria will not be exceeded.
Feedwater Temperature Reduction Analyses are performed in order to justify operation at a reduced feedwater temperature at rated thermal power. Usually, the analyses are performed for end-of-cycle operation with the last-stage feedwater heaters valved out of service.
However, throughout cycle operation, an additional feedwater temperature reduction can be justified by analyses at the appropriate operating conditions.
The limiting AOTs are reanalyzed for operation at a reduced feedwater temperature.
In addition, the loss-of-coolant accident (LOCA), fuel loading error, rod drop accident, and rod withdrawal error are also re-evaluated for operation at a reduced feedwater temperature.
3.7-22
BFN-26 Turbine Bypass Out of Service Operation of the turbine bypass system is assumed in the analysis of the Feedwater Controller Failure (FWCF)-maximum demand event. If this event is limiting or near limiting, the operating limit MCPR basis may be invalid if the bypass system cannot be demonstrated as fully functional. Reload specific evaluations may incorporate a FWCF without credit for bypass operation calculation as a provision when temporary factors render the system unavailable. Additionally, for extended operation with degraded bypass system operation, evaluations in support of this condition are augmented with the appropriate limiting events, such as the FWCF, for the applicable cycle.
ARTS Program The ARTS program is a comprehensive project involving the Average Power Range Monitor (APRM), the Rod Block Monitor (RBM), and Technical Specification improvements.
Implementing the ARTS program provides for the following improvements which enhance the flexibility of the BWR during power level monitoring.
(1) The Average Power Range Monitor (APRM) trip setdown requirement is replaced by power-dependent and flow-dependent MCPR operating limits to reduce the need for manual setpoint adjustments. In addition, another set of power- and flow-dependent limits (LHGR and/or MAPLHGR) are also specified for more rigorous fuel thermal protection during postulated transients at off-rated conditions. These power- and flow-dependent limits are verified for plant-specific application during the initial ARTS licensing implementation. For GE reload analyses, these limits are verified to be applicable to subsequent cycles provided that there are no changes to the plant configuration as assumed in the licensing analyses. For AREVA reload analyses, the power-and flow-dependent limits are reviewed and updated as needed each cycle.
(2) The RBM system is modified from flow-biased to power-dependent trips to allow the use of a new generic non-limiting analysis for the Rod Withdrawal Error (RWE) and to improve response predictability to reduce the frequency of nonessential alarms. The applicability of the generic RWE analysis to GE fuel designs is discussed in Reference 10. For AREVA reload analyses, the RWE analysis with ARTS is re-evaluated each cycle.
The resulting improvements in the flexibility of the BWR provided by ARTS are designed to significantly minimize the time to achieve full power from startup conditions.
3.7-23
BFN-26 Recirculation Coolant Pump Out of Service The plant is licensed to allow extended Single-Loop Operation (SLO). The capability of operating at reduced power with a single recirculation loop is highly desirable, from a plant availability/outage planning standpoint, in the event maintenance of a recirculation pump or other components renders one loop inoperative. SLO analyses evaluate the plant for continuous operation at a maximum expected power output.
To justify SLO, safety analyses have to be reviewed for one-pump operation. The MCPR fuel cladding integrity safety limit, AOT analyses, operating limit MCPR, and non-LOCA accidents are evaluated. Increased uncertainties in the total core flow and traversing incore probe (TIP) readings result in a small increase in the fuel cladding integrity safety limit MCPR.
SLO can also result in changes to plant response during a LOCA. These changes are accommodated by the application of reduction factors to the two-loop operation LHGR and/or MAPLHGR limits, if required. Reduction factors are evaluated on a plant and fuel type dependent basis. In each subsequent reload, reduction factors are checked for validity and, if new fuel types are added, new reduction factors may be needed in order to maintain the validity of the SLO analysis.
End-of-Cycle Recirculation Pump Trip Out of Service The EOC-RPT-OOS contingency mode of operation eliminates the automatic recirculation pump trip signal when turbine trip or load rejection occurs. As such, the core flow decreases at a slower rate following the recirculation pump trip due to the anticipated transient without scram (ATWS) high pressure recirculation system trip, thus, increasing the severity of the transient responses.
Power Load Unbalance Out of Service The load rejection event scenario depends on whether the initial power level is sufficient for the PLU feature to operate. The PLU causes fast closure of the TCV.
If the PLU does not operate as the result of a load rejection, the TCV closes at the maximum demand rate for speed control (servo mode). For the PLUOOS analysis, the PLU is assumed inoperable at any power level and does not initiate fast TCV closure.
3.7.7.3 Core Hydraulics Core hydraulics models and correlations are discussed in Subsection 3.7.5, Description of Thermal-Hydraulic Design of the Reactor Core.
3.7-24
BFN-26 3.7.7.4 Influence of Power Distributions The influence of power distributions on the thermal-hydraulic design is discussed in Reference 13.
3.7.7.5 Core Thermal Response The thermal response of the core for accidents and expected AOT conditions is given in Chapter 14, Plant Safety Analysis.
3.7.7.6 Analytical Methods The analytical methods, thermodynamic data, and hydrodynamic data used in determining the thermal and hydraulic characteristics of the core are documented in Subsection 3.7.7.1.2, MCPR Operating Limit Calculational Procedure.
3.7.8 References
- 1. General Electric Standard Application for Reactor Fuel, NEDE-24011-P-A, (See Appendix N for applicable revision).
- 2. Core Flow Distribution in a Modern Boiling Water Reactor as Measured in Monticello, NEDO-10299A, October 1976.
- 3. H. T. Kim and H. S. Smith, Core Flow Distribution in a General Electric Boiling Water Reactor as Measured in Quad Cities Unit 1, NEDO-10722A, August 1976.
- 4. Brunswick Steam Electric Plant Unit 1 Safety Analysis Report for Plant Modifications to Eliminate Significant In-Core Vibrations, NEDO-21215, March 1976.
- 5. Supplemental Information for Plant Modification to Eliminate Significant In-Core Vibration, NEDE-21156 (Proprietary), February 1976.
- 6. General Electric Standard Application for Reactor Fuel (Supplement for United States), NEDE-24011-P-A-US, (See Appendix N for applicable revision).
- 7. R. C. Martinelli and D. E. Nelson, Prediction of Pressure Drops During Forced Convection Boiling of Water, ASME Trans., 70, 695-702, 1948.
- 8. C. J. Baroozy "A Systematic Correlation for Two-Phase Pressure Drop," Heat Transfer Conference (Los Angeles), AICLE, Preprint No. 37, 1966.
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BFN-26
- 9. N. Zuber and J. A. Findlay, Average Volumetric Concentration in Two-Phase Flow Systems, Transactions of the ASME Journal of Heat Transfer, November 1965.
- 10. General Electric Fuel Bundle Designs, NEDE-31152P, Rev. 7, June 2000.
- 11. W. H. Jens and P. A. Lottes, Analysis of Heat Transfer, Burnout, Pressure Drop and Density Data for High Pressure Water, USAEC Report-4627, 1972.
- 12. NRCB 88-07, Supplement 1, Power Oscillations in Boiling Water Reactors (BWRs), December 30, 1988.
- 13. General Electric BWR Thermal Analysis Basis (GETAB): Data, Correlation, and Design Application, NEDE-10958-PA and NEDO-10958-A, January 1977.
- 14. Methodology and Uncertainties for Safety Limit MCPR Evaluation, NEDC-32601P, August 1999.
- 15. Power Distribution Uncertainties for Safety Limit MCPR Evaluations, NEDC-32694P, August 1999.
- 16. Qualification of the One-Dimensional Core Transient Model for BWRs, NEDO-24154, Vol. 1 and 2; October 1978.
- 17. Qualification of the One-Dimensional Core Transient Model for BWRs, NEDE-24154-P, Vol. 3; October 1978.
- 18. Steady-State Nuclear Methods, NEDE-30130-P-A and NEDO-30130-A, April 1985.
- 19. Letter from J. S. Charnley (GE) to C. O. Thomas (NRC), Amendment 11 to GE LTR NEDE-24011-P-A, February 27, 1985.
- 20. Impact of Time Varying Axial Power Shape on Pressurization Transients, GENE-666-03-0393, March 1993.
- 21. R. B. Linford, Analytical Methods of Plant Transient Evaluations for the General Electric Boiling Water Reactor, NEDO-10802, February 1973.
22 R. B. Linford, "Analytical Methods of Plant Transient Evaluations for the GE BWR Amendment No. 1," NEDO-10802-01, June 1975.
- 23. R. B. Linford, Analytical Methods of Plant Transient Evaluations for the GE BWR Amendment No. 2, NEDO-10802-02, June 1975.
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BFN-26
- 24. Letter from R. E. Engel (GE) to T. A. Ippolito (NRC), Change in GE Methods for Analysis of Cold Water Injection Transients, September 30, 1980.
- 25. Determination of Limiting Cold Water Event, NEDC-32538P-A, February 1996.
- 26. Letter from K. W. Cook (GE) to F. Schroeder and D. G. Eisenhut (NRC),
Implementation of a Revised Procedure for Calculating Hot Channel Transient CPR, July 20, 1979.
- 27. Letter from R. C. Tedesco (NRC) to G. G. Sherwood (GE), Acceptance for Referencing General Electric Licensing Topical Report NEDO-24154/NEDE-24154P, February 4, 1981.
- 28. Letter from J. S. Charnley (GE) to C. O. Thomas (NRC), Supplementary Information Regarding Amendment 11 to GE Licensing Topical Report NEDE-24011-P-A, October 9, 1985.
- 29. Letter from R. A. Bolger (Commonwealth Edison Co.) to B. C. Rusche (USNRC),
QC-2 Proposed Amendment to Facility License No. DPR-30, Docket No. 50-265.
- 30. Letter from R. E. Engel (GE) to T. A. Ippolito (NRC), End of Cycle Coastdown Analyzed With ODYN/TASC, September 1, 1981.
- 31. Letter from J. F. Klapproth to the NRC Document Control Desk, Rectification of Inconsistency in One Dimensional Core Transient Model, MFN-176-93, October 29, 1993.
- 32. ANF Critical Power Methodology for Boiling Water Reactors, ANF-524(P)(A)
Revision 2 and Supplements 1 and 2, Advanced Nuclear Fuels Corporation, November 1990.
- 33. Methodology for Calculation of Pressure Drop in BWR Fuel Assemblies, XN-NF-79-59(P)(A), Exxon Nuclear Company, November 1983.
- 34. Siemens Power Corporation Methodology for Boiling Water Reactors:
Evaluation and Validation of CASMO-4/MICROBURN-B2, EMF-2158(P)(A)
Revision 0, Siemens Power Corporation, October 1999.
- 35. MICROBURN-B2: Theory Manual, FS1-0009248 Revision 1, AREVA NP Inc.,
January 2013.
- 36. (Deleted).
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BFN-26
- 37. XCOBRA-T: A Computer Code for BWR Transient Thermal-Hydraulic Core Analysis, XN-NF-84-105(P)(A) Volume 1 and Volume 1 Supplements 1 and 2, Exxon Nuclear Company, February 1987.
- 38. (Deleted).
- 39. Letter, T. A. Galioto (FANP) to J. F. Lemons (TVA), Browns Ferry Unit 3 Cycle 12 MCPR Safety Limit Analysis Revision 1 Core Design, TAG:04:018, January 30, 2004
- 40. COTRANSA2: A Computer Program for Boiling Water Reactor Transient Analyses, ANF-913(P)(A) Volume 1 Revision 1 and Volume 1 Supplements 2, 3, and 4, Advanced Nuclear Fuels Corporation, August 1990.
- 41. Exxon Nuclear Methodology for Boiling Water Reactors, THERMEX: Thermal Limits Methodology Summary Description, XN-NF-80-19(P)(A) Volume 3 Revision 2, Exxon Nuclear Company, January 1987.
- 42. ANP-10307PA Revision 0, AREVA MCPR Safety Limit Methodology for Boiling Water Reactors, AREVA NP, June 2011.
- 43. SPCB Critical Power Correlation, EMF-2209(P)(A) Revision 3, AREVA NP, September 2009.
- 44. Application of Siemens Power Corporations Critical Power Correlations to Co-Resident Fuel, EMF-2245(P)(A) Revision 0, Siemens Power Corporation, August 2000.
- 45. Letter from Ralph J. Reda to R. C. Jones, Jr., Implementation of Improved GE Steady-State Nuclear Methods, Letter No. MFN-098-96, July 2, 1996.
- 46. ANP-10298PA Revision 0, ACE/ATRIUM 10XM Critical Power Correlation, AREVA NP, March 2010.
- 47. ANP-3140(P) Revision 0, Browns Ferry Units 1, 2, and 3 Improved K-factor Model for ACE/ATRIUM 10XM Critical Power Correlation, AREVA NP, August 2012.
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