ML19290A296
| ML19290A296 | |
| Person / Time | |
|---|---|
| Site: | Crane  |
| Issue date: | 10/25/1979 |
| From: | Marino G, Marks J NRC OFFICE OF NUCLEAR REGULATORY RESEARCH (RES) |
| To: | NRC OFFICE OF NUCLEAR REGULATORY RESEARCH (RES) |
| References | |
| NUDOCS 7911060097 | |
| Download: ML19290A296 (75) | |
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MEMORANDUM FOR: Files FROM:
G. P. Marino Fuel Behavior Research Branch J. M. Marks
- Fuel Behavior Research Branch
SUBJECT:
CALCULATION OF FUEL R0D TEMPERATURES REACH.~D IN THE THREE MILE ISLAND-2 INCIDENT I.
INTRODUCTION Soon after the TMI-2 incident, several attempts were made in the Fuel Behavior Research Branch to compute the fuel rod temperatures reached during the incident. These early calctlations (see Refereines 1 and 2) were necessarily rudimentary and involved several ro_ ugh assumptions due to the time factor involved and the paucity of data concerning the actual sequence of events available at that time.
In particular, it was assumed that thi core water level drcpped at a rate of about 12-14 feet per hour for approximately 30 minutes and held at the 5-or 6-foot level from the bottom of the core for another 30 minutes before refilli.ng took place. Moreover, the uncertainty and difficulties associated with cunputing the complex nature of the heat transfer mech-anisms during the core-water boildown led to simplistic assumptions of
- J. M. Marks ts currently at the Massachusetts Institute of Technology where he returned after sumer employement at the NRC, Of ? ice of Research. He was responsible for generalizing the existing computer tode, but should not be held responsible for the conclusions and later madeis presented herein.
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'- # Files OCT 2 51979 adiabatic rod heat-up with a ~25 perc6nt heat loss to the steam and neigh-
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boring cold rods. No attempt was made to compute the effects of steam heat-up, oxidation-generated heat, radiative heat transfer, and varying reactor pressure on the overall heat transfer process. However, oxida-tion heat was later added to the power input to the rod.
In brief, the results of such calculations showed that, dependi.ng on the axialandradialpositionsoftherod,therodhe(t-upratesrangedfrom approximately 1*F/see to approximately 3'F/sec.
It was also shown that only about 3 percent of the available decay heat was required to heat the steam; at the same rate as the rods, given the assumption of a stagnant steam bubble condition. Later information from the plant indicates that significant steam flow did occur duri.ng the boildown; and, if so, its heat-removal capability should be considered.
The purpose of this memorandum is to document a more detailed calculation of the TMI-2 core temperatures using a computer code developed in-house which accounts for core water level as a function of time, variable water / steam properties, oxidation heat, temperature varyi_ng fuel rod material properties, steam flow rate, and a best-estimate rod-to-steam heat transfer coefficient. The tentative name given to the computer code is TMIBOIL.
II. ANALYSIS Consider a'si.ngle fuel rod bei.ng uncovered at a rate R ft/hr with steam flowtng past it at a velocity v ft/hr. The parameter, R, is, in general, a function of the amount of core still covered; and, thereby, depends on 2224 245
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Files OCT 2 51979 the amount of water being added to, and subtracted from, the core via safety injection systems, leaks, steam condensation, and storage tanks.
It was decided, therefore, to treat the uncovery rate, R, as an indepen-
' dent input parameter due to the uncertainty as to the exact water removals and additions as a function of time. The parameter, y, depends only upon the amount of core still covered and was, therefore, calculated throughout the analysis.
A heat balance on an axial element of the rod dx thick at axial position x(wherex=0correspondstothetopofthecore) yields:
2 P(x)dx = C pur _a_T, dx + h (T(x,t)-T (x,t)) 2nrdx (la)
T s
P at where:
C is the averaged specific heat of the rod (BTU /lb);
p 3
a is the averaged density of the rod Obs/ft );
ristherodradius(ft);
2 h is the rod to steam heat transfer coefficient (BTU /hr-it,
- r;;
T is the rod temperature (*F) at x and time, t; T is the steam temperature (*f) at x and time, t; s
P(x) is the rod power per unit le_ngth at position x (BTU /hr-ft)
Dividi.ng through by dx gives:
2 BT + 2nrh (T(x,t)-T (x,t))
Ob)
P(x) = C pur s
P at 2224 246
A.-...-.._-..._._.._....____._._.__________.
Files -
OCT 2 51979 A corresponding heat balance for.the steam at position x yields:
~
p Ay s
(2) 2nrh(T(x,t)-T(x,t))=C P Ah+C s
s s s
ps s Where the subscript s refers to steam properties, and v is the steam velocity.
A, is the cross-sectional area of coolant channel per rod, and the term BT /ax is the_ gradient of the steam temperature over the length s
dx.
Equations (1b) and (2) can be solved by usi.np finite-difference techniques on a computer. The method used was a time implicit technique applied to equations (1b) and (2) in finite-difference form in the following For a time interval at (approximately 20 seconds) equations (1b) manner.
and (2) can be written in approximate form as:
r (T-T ) + C ((T+T ) - (T +Tsi))
(3),and Pat = B j
j 3
C((T-T)-(T+Tg )) = B (T -Tsi)+D((T+Tsi) - (T b+Tg ))
(4) b j
s s s 3
s 2
PA Also, T is ps s s, C=nrhat, and D=p vA c at/2dx.
where B =C onr, B =C s s p
s the final (at end of time step) temperature of the element dx averaged over its length. T is the corresponding steam temperature, T$ and Tsi s
are the spatially averaged initial rod and steam temperatures, respectively, and T and T b are the correspondi_ng spatially averaged fuel and initial g
steam temperatures of the elemental node just below the node considered.
The inherent assumption in the last term of equation (4) is that the axial gradient in the steam temperature is linear over a distance of two nodal,spaci.ngs. Calculated steam temperature profiles from the code indicate that this is a very good assumption for the values of dt (20 sec) and dx (1") used.
2224 247
R.
._...s.._..
. _. _.. ~. _ _. _. _. -. _.
Files OCT 2 51979 Equation (3)and(4)aboveweresolvedsimultaneouslyforTandT;the s
solutions of which are too lengthy and complex to be repeated here.
However, given the results, a computer code was developed containing a generalized sequence of boiloff conditions to compute the rod and steam temperatures at 1-inch space intervals and 20 second time intervals for an average rod of a given bundle of the core.
It should be noted that for an axial node just being uncovered over a_ givkn time step, equations (3) and (4) were modified for time-averaged heat transfer values by halving the power term in equation (3) and halving the rod to steam heat transfer (the constant C) in both equations (3) and (4). No other modi-fications were necessary.
Account is taken of the heat generated via the Zircaloy-water exothermic reaction by addi.ng it to the power tenn, P, in equation (3). The oxida-tion power term is calculated from the Cathcart-Pawel correlation equa-tions given in the MATPRO manual (Reference 3). Since the power generated by oxidation is itself temperature dependent (in exponential fonn), the oxidation heat computed from the previous time step was added to current heat terms. Thus, the oxidation heat is treated by explicit calculational techniques. Other models required for a successful formulation of the problem included an axial peaking factor model, hydrogen generation model, oxide thickness model, fuel rod specific heat model, temperature varying fuel rod property models, a steam starvation check, and tempera-ture and pressure dependent water and steam properties.
2224 248
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OCT 2 51978 Flies -
The axial peaking factor (APF) mode 1 ~was derived from a curve of the APF as a function of. axial distance from the core top for the_TMI-2 reactor.
The curve was obtained from the Babcock and Wilcox Company by M. L. Picklesimer of the FBRB. F.igure1showstheAPFversusdistancecurve(solidline).
Ananalyticalfunctionwasderivedtofitthecurvebytheauthors$the results of which are shown as circles on the graph. The functional form used is also depicted on the figure in terms of the axial distance from the top of the core (x). The other models in the code will be described in the followi.ng section.
III. CODE DESCRIPTION The code begins its calculations by assumi.ng that at time zero the core is just fully covered and b_egins to boil away. A function subroutine -
ALEVEL'- allows one to input the water level height as a series of ramp segments versus time. As stated before, this subroutine is necessary because of the unknown additions and subtractions of coolant that occurred during the tine period; and, therefore, the level cannot simply be calcu-lated from the boiloff rate. However, the boiloff rate and, therefore, the steam mass flow rate must be calculated for use in the computation of the steam cooling effect on the rods. This latter calculation considers the axial peaking factor profile, described earlier, and depends only upon the amount of core still covered.
l 2224 249
L...
.:...c...-..-.------------------
Y OCT 2 51979 Files A time' step is taken,'of approximately 20 seconds,'and the core level is adjusted from the ALEVEL function.
Rod temperatures are calculated at 1-inch intervals so that an axial node is considered covered until more than half of it is uncovered. Then it is assumed to be fully uncovered.
The code proceeds in this manner for each time step computing more and more axial segments as the core level decreases.
For each axial segment and time step, the oxidation reaction is accountep for as follows:
A.
The new temperature of the node is computed assuming power from decay heat and the oxidation heat from the previous time step B.
The amount of new oxidation that occurred, the hydrogen generated.
(and,therefore,theamountofsteamrequired)andtheoxidation heat generated are then calculated.
C.
The oxidation heat generated is then stored to be added to the decay heat for the next time step.
D.
The code then advances to the next axial rode.
Note that the mode of calculation does not allow for oxidation heat feedback during the time step, but feeds back only in the next time step.
The amount of hydrogen generated is summed for each node, each time step,
'and printed as output.
l 2224 250
. ~.. _ _ _ _
' - Files OCT 2 51979 After each time step a check is _made to determine whether enough steam was_ generated to supply the oxidation reaction over the entire rod with sufficient steam.
If steam starvation occurs, a message is printed out
~
warning the user of the event.
The specific heat of the fuel and claddi.ng at each axial node are computed as a function of teinpetature at the beginni.ng of each time step using the MATPRO correlations. The reactor pressure is inpd as a function of time in 2.5 minute intervals as read from actual TMI-2 strip charts beginning at 100 minutes into the accident.
From this input, the water satur,ation temperature, the heat of vaporization of the core water, and the steam specific heat are also computed at the beginni.ng of each time step. These calculations use correlations of the above properties derived from steam tables. The steam specific heat correlation was taken from a paper by Rivard and Torrey (Reference 4).
The rod to steam heat transfer coefficient was initially input parametrically as a constant value throughout the computation period.
However, because of the high temperatures predicted, this procedure was modified later to account for the strongly temperature dependent radiative heat transfer mechanism from the rod to steam. The coefficient used was taken from the correlation equation used in the RELAP thenna1 hydraulics code. Thus, h=h
+h (5)where, c
rad h
= 3.942 x 10@ (T 4-Ts )/(T -T ) BTU /hr-Ft
- F, (6),and 2
rad p
rs 2224 251
............. ~.. - - - -. - - -. -.... - -....... - -....
e......--.
007 2 5 1979
.. Files h is the convective heat transfer coefficient for naturally circulating c
steam and used parametrically in the code.
In succeeding sections of 2
this report, the heat transfer units of BTU /hr-Ft
- F will be shortened toe.U.(Englishunits).
Finally, the code can provide the user with rod temperature versus time plots at various axial positions, rod temperature versus distance plots at various times, and a core level versus time plot from the ALEVEL subroutine.
It should be kept in mind that the fuel rod is assumed to remain intact throughout its temperature history regardless of the temperatures reached, although the oxidation reaction is programmed to cease at any axial node which exceeds the oxygen-saturated cladding melting temperature (approximately 3600F).
IV. RESULTS The code was run for the following scenarios of core water level. All distances are from the bottom of the core.
A.
The core water level decreased at a rate of 14 feet / hour to the 5-foot leyc1 (30 minutes), held constant at 5 feet from the bottom for 30 additional minutes, and refilled.
l 2224 252
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.............----....-.a.--.-.:.----.....------..-~------
F es Oct 2 s 1979
-B.
The core water level decreased at a rate of 14 feet / hour to the 5-foot level (30. minutes), held constant at 5 feet for an additional 50 minutes, and refilled.
C.
The core water level decreased at a rate of 14 feet / hour to the 4-foot level (34 minutes), held constant at 4 feet for an additional 46 minutes, and refilled.
D.
The core water level decreased at a rate of 14 feet / hour to the 3-foot level (38.5 minutes), held constant at 3 feet for an additional 41.5 minutes, and refilled.
All the models described above were not put into the code initially in order to check out their effect on the results as they were added.
During this development period only scenario (A) was used. Examples of the results obtained will be presented chronologically and in order of increasing code complexity to illustrate the sensitivity of the results to the models added.
A.
Base ~ Case A - Models and Assumptions 1.
he oxidation heat model.
2.
Constant water properties (P=900 psi, TSAT=560F).
3.
Constant rod and steam specific heats.
4.
h=h only, where h is treated parametrically.
e c
5.
, Scenario (A) for boildown history.
6.
Radial peaking factor of 1.467 (hot bundle).
7.
Decay heat factor of 1.1 percent.
2224 253
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.....;_.;......._.._....u.._.-.._......._......_..._.._.......
OCT 2 5 N79 Files '
Figures 2 and 3 show typical results (rod tJnperature Versus time) m:
.obtained for assumed h-values of 3.0 and 10.0 E.U.
The numbers on the plots refer to the axial level from the top of the core in feet.
Note that in both cases the claddi.ng temperature remains below its melting point. Also, increasi.ng the assumeA h-value from 3 to 10 lowers the temperature at 60 minutes from 2900'F to about 2500 F.
It also has the effect of shifting the hottest portion of the rod from the 2-foot level to the top level of the rod. The reason for this effect is that the higher heat transfer increases the local steam temperatures to the point that the upper portion of the rod is heated by hot steam from the lower levels. The effect overcomes the fact that the 0-foot level is at a considerably lower decay heat power level (see Figure 1) than the 2-foot level.
B.
Case'B~- Base Case A With the Oxidation Heat Model Added F.igures 4 and 5 show the tremendous effect of adding the oxidation heat model. At temperatures near 2600*F, the power generated by the oxidation reaction overwhelms the decay heat power and produces unrealistically high temperatures. The fall-off of the high tempera-ture spikes is caused by the loss of oxidation heat due to completion of oxidation of the claddi_ng at that point. Note that an increase in h-value shifts the breakaway point to longer times, reduces the le.ngth along the rod over which breakaway occurs, and reduces the l
2224 254
i... e
. ~. _..
-- -........ ~..:...
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Ffles OCT 2 51979 unrealistically high peak rod temperatures. We also note here that the extremely rapid oxidation reduces code accuracy near the spike r.egion so that a reduction in assumed time step from 20 seconds to 10 seconds gives slightly differing code results. Without the oxidation model, code results were identical for time steps of 10 or 20 seconds. Obviously, the above :esults are not physically realistic since melting of clad and fuel will occur lofig before such tempera-tures can be reached.
In fact, rod heat-up experiments, conducted by Hagan at KfK, have clearly shown that at temperatures in the range 3400-3600 F, oxygen-saturated cladding reacts with the hypo-stoichiometric Zr02 present on the clad surface to form a liquid eutectic mixture of zirconium and oxygen. He also showed that the liquid flowed into the fuel-clad annular. gap and reacted with the fuel to form another liquid mixture of U-Zr-0 which slumped or flowed to the bottom of the rod.
C.
Case C - Case B'With 0xidation Cut 0ff Model In order to provide a conservative mechanism for the shutoff of the oxidationreaction(andtheheatproducedbyit),thecodewas modified to cease oxidation at any node which reached 3600'F. This temperature is the maxirrum melting point of Zr containing oxygen and is about 150 F higher than the temperature of formation of the Zr-Zr02 eutectic liquid. This brings us to our next set of results.
l 2224 255
F1'les OCT 2 51979 Figures 6 and 7 give the results of the addition of the oxidation cutoff model at 3600'F. Note the large decrease in peak cladding temperature. The relative effect of increasing the h-value is about the same as for the results without the cutoff. The effect of the cutoff model is simply to truncate the peak temperatures of those regions of the rod which achieved temperatures where rapid oxidation begins. The truncated peak then decreases ip temperature because the decay heat alone is not sufficient to maintain the 3600 F peak temperature obtained using oxidation heat.
In fact, each axial position approaches asymptotically the steady-state temperat6re it "would have for the steady final steam mass flow rate of scenario (A); i.e., 2.46 lbs. steam / hour / rod.
D.
Case D - Case C'Witn Temperature Varving Rod' Specific Heat The result for this case, which added temperature dependent correlations for the specific heats of the cladding and fuel, is given in Figure 8 for an h-value of 3.0 E.U.
Direct comparison with Figure 6 shows that the addition of a more refined rod specific heat model has only a sl.ight effect on the results.. The heat-up rate: are sl.ightly slower due to the increase in the specific heat of both fuel and cladding as temperature increases. However, the model had little or no effect on determining how much of the rod reached the clad melt-1.ng temperature of 3600*F.
i
'u:
2224 256
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Files
.. OCT i. m.;
E.
Case'E'- Case D'Plus Time-Dependent Reactor Pressure, Saturation
- ' Temperature, and Heat of Vaporization In this model, the actual recorded pressure of the TMI-2 reactor was input in 2.5 minute intervals starting from 100 minutes into the transient to 160 minutes. The objective was to determine the effect of reactor pressure ranging from 1005 psi to 670 psi to 907 psi.
The results are shown in F.igure 9 for h=3.0 E.U.
Comparison with Figure 8 shows again only a slight decrease in heat-up rate and no significant overall effect for this scenario. At this point-in the
" code development, the code did not have a correlation for the steam specific heat as a function of temperature and pressure; a constant value of 0.52 BTU /lb *F was used.
F.
Case F - Case E With~ Additions of Steam Specific Heat Correlation
'and Scenario (B)
Figures 10 and 11 show the effect of using a variable steam specific heat model from Reference 4 as a function of pressure and temperature.
In these two figures the scenario was changed to include an addi-tional 20 minutes at the core water level of 5 feet. This later change had no effect, of course, on the temperature history to the 60-minute mark. However, it does allow for an increase in reactor pressure from the previous value at 60 minutes (907 psi) to 1410 psi at 60 minutes into the uncovery period. Comparing the f.igures shows that the more accurate steam specific model further reduced the h
heat-up rate of the rod, but did not prevent the first 5 feet of the core from reachi.ng the clad melting temperature.
2224 257
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Files G.
' Case G'- Case'F'With' Addition'of Radiative Heat' Transfer Model The last model added to the code was a radiative heat transfer model from the RELAP code.
It was expected that at temperatures exceedi_ng approximately 2500*F, this mode of heat transfer would overwhelm that due to unforced convection of steam (h = 3.0 E.U.).
Figure 12 c
shows the large effect this addition made to, the predicted tempera-ture history. Note that for this boildown scenario (B), no part of the rod exceeded 3200*F; and, therefore, no clad melting would be expected. Note also that only the top of the rod exceeded 3000 F, whereas, from the 1-foot level to the 6-foot level, temperatures were below 2400*F. This result shows the major importance that must be attached to radiative heat transfer at temperatures greater than 2000 F in naturally circulating steam.
Inclusion of this model conclutad the planned additions to the code. Attention was, therefore, turned to the effect of the assumed boildown scenario. To test this effect, scenario (D) was used which allowed the core water level to decrease to the 3-foot level at a rate of 14 feet per hour and be held at that level for the remaini.ng period.
Figure 13 shows the results of that run. Comparison vith Figure 12 shows the very la.rge effect of boildown history. One should remember that this run included all the sophisticated r odels mentioned above includi.ng the radiative heat transfer model, Note that now at least 5 feet of the core achieved temperatures iii excess of the cladding melt temperature, 2224 258
u...
.............. ~.......
.. - -. ~. - - - - -. -.
Files OCT 2 51979 whereas, for scenario (B) (level decreased to 5 feet) none of the claddi.ng was predicted to melt. The continued rise in temperature of these areas (oxide shells) beyond the clad melting temperature is due to fact that the mass. flow rate of steam at the 3-foot level was not sufficient for cooling the upper part of the core below 3600'F in spite of the increased heat transfer. Because of the large effect of the bo11down scenario, an additionil problem was run under conditions intermediate between scenarios (B) and (_0).
Scenario (C) allows the core water level to decrease to the 4-foot level. The results are :;hown in Figure 14. As expected the results are inter-mediate between those of the other two scenarios, and shows clad melting of about the upper 3 feet of the L.,.a.
These results clearly illustrate that any accurate analysis of the core damage experienced by the TMI-2 reactor requires accurate information as to the core water level history for the first uncovery period.
V.
CONCLUSIONS This report describes a computer code (TMIBOIL) to analyze the core temperatures reached in the TMI-2 incident at Harrisburg, Pennsylvania.
It is basically a time-implicit,-finite-difference solution to the heat equation and includes such models as oxidation heat, radiative and con-yective k' eat transfer. hydr. ogen generation calculations, variable reactor 2224 259
2."
...... : =. :.. =:w w..., - -. =.
.u. ;...........
25M pjles pressure, stear : sage calculations,' cladding thickness and oxide thickness model, steam table correlations for core saturation temperatures, heats of vaporization, steam specific heat, and MATPRO correlations for fuel and cladding specific heats.
Included also is an axial peaking factor model based on the THI-2 reactor. The code can easily be generalized to handle any sequence of core-water level history and cou!c ce extended to other types of reactors. Appendix A contains theJORTRAN listi.ng of the code and some sample problem results.
Important findings of this study are:
A.
Clad melting may or may not have occurred in TMI-2 dependi.ng upon whether the core-water level decreased below the 5-foot level or not.
B.
The exact boildown histor, is required to accurately assess the core damage.
C.
Radiation heat transfer to steam cannot be neglected in the analysis.
D.
The calculations are relatively insensitive to exact modeling of the fuel, clad, and steam specific heats compared to the effect of Dolldown history and radiative heat transfer.
E.
Cladding oxidation heat is a major factor in rapid heat-up of the core when clad temperatures exceed approximately 2400'F.
l 2224 260
F1"les OCT 2 51979 F.
Oxidation heat must be cutoff at the cladding melting temperature to realistically describe the fuel temperature history. The amount of claddi.ng remaini.ng when clad melting occurs ra_nged from 16-18 mils out of an initial 26.5 mils.
G.
No steam starvation occurred for any calculation that included the oxidation cutoff model.
The reader is cautioned that the code described above has not been fully verified as yet.
Initial verification via checking steady-state results with z. closed-form solution was made and showed the code to be operating correctly. Moreover, individual model computations were checked usi_ng a hand calculator.
Full verification may not be possible due to lack of experimental data to check against.
/fdv George P. Marino Fuel Behavior Research Branch Division of Reactor Safety Research tb 1/AlW/S:Ad
[7)l.wh J. M. Marks Fuel Behavior Research Branch Division of Reactor Safety Research
Enclosures:
As stated cc: See next page 2224 261
+.. -
REFERENCES 1.
Memorandum for Filas, G..P. Marino, April 25, 1979, " Preliminary Assessment of Core Damage for Three Mile Island Incident."
2.
Memorandum for Files, M. L. Picklesimer, June 20,1979, " Bounding Estimates of Damage to Zircaloy Fuel Rod Cladding in the TMI-2 Core at Three Hours After the Start of the Accident, March 28, 1979."
3.
MATPRO-VERSION II, "A Handbook of Material Properties for use in the Analysis of Light Water Reactor Fuel Rod Behavior," D. L. Hagrman, G. A. Reymann Eds, February 1979.
4.
LA-6104-MS, " Numerical Calculation of Flashing from Long Pipes Using a Two-Field Model," W. C. Rivard and M. D. Torrey, November 1975.
222:4 262
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_. - _. _.. _ _, _ ~. _.. _ _ _
ACKNOWLEDGMENTS The authors vcold like to express their gratitude and appreciation to M.
L. Picklesimer, R. R. Sherry, and D. A. Hoatson, of the Fuel Behavior Research Branch, for their mi.- stimulating discussions and suggestions during the formulation of this computer code.
We also express our thanks to A. Serkiz, of RSR, for suggesting the importance o' the radiative heat transfer term and to N. Lauben, of DSS /NRR, for supplying the equation from the RELAP code.
e e
h 2224 263
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FIGURE 1 Axial Peaking Factor Versus Axial Distance APF = 0.25 + 1.10 SIN (wx/12) + 2.2 SIN (W(x +.7)/4.2) x is in feet
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0 5-1.G KPoints are Calculated af
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2224 264 0
k k
8 8
'o J2 Bottom top Axial Distance (ft)
E p.
i FIGURE 2
$..i; No Oxidation Model-H=3 E.U.
FUEL IEMormatuRE HISTonIFS OF 1 FT NODES 3000e..............+.......................................+..........t....+.......+
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9
- f. 7 FIGURE 9 e,,
With Variable Reactor Pressure Model t
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FIGURE 10 PANEL-1 F31RI 1
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0 8.00 16.00 24.00 32.00 40.00 48.03 56.03 64.0) 72.0) 8-3.03 TIME - 51 NOTES
APPENDIX _A 1.
//GPMTMIB JOB (WDCC,361,B),MARIND 3.
// MAIN EXEC FORGCOMP 4.
// COMP.SYSIH DD M 5.
CMMMM SPATIAL AVERAGING FUNCTION OF AXIAL PEAKING FACTOR 6.
APFB(X1,X2)
(0.25M(X2-XI)+4.202MCCOS(3.14159MX1/12.)
7.
X-COS(3.14159MX2/12.))+0.283MCCOSC3.14159MCX1+0.7)/4.2)-
8.
XCOSC3.14159M(X2+0.7)/4.2)))/(X2-X1) 9.
HTC(Z) : 3.
.10.
CPRDT(T1,T2) =0 11 CPWDT(T1,T2) =0 l
12.
COMMON /COMZR/ROR.DTIME,THC,XOF i
12.1 COMM0H/C0ZR/DENSF.DENSC,RIC,ROF 12.2 COMM0H/COMRT/ PRES,5GT.IEMOV.PTIME,STIME,BTIME, METHOD.0PTION,IDIVP l'
13.
DIMENSIGH PRES (60),SGT(60),IEMOVC60), NODE (13),APFC170),
i 14.
XTMR(170),TMSC170),X0IC170),TR(14,600) TS(14,600),KMELT(170),
l 15.
XCH2(600),PTIME(60),STIME(60),BTIME(60) ECTC600) ECHC170),
.16.
XWLEVEL(600),ZR(14,600).TP(14,600),
' 17.
XTPS(14,600),YARY(600), CHAR (10),TDELT(170),ZRGEN(170)
' 18.
REAL MDOT,HPOW,MINTME l
19.
DATA CHARC1), CHAR (2), CHAR (3), CHAR (4),CHARC5), CHAR (6), CHAR (7),
i 20.
XCH AR(8 ), CH AR( 9), CH AR( 109/ ' 0 ', ' 1 ', ' 2', ' 3 ', ' 4 ', ' 5 ', ' 6 ', ' 7 ', '8 ',
l 21.
X'9'/
22.
CMMMM INITIALIZE PROGRAM PARAMETERS e
23.
CMMMM OUTPUT OPTIONS l
24.
CMMM DO NOT PRINT / PLOT RESULTS IF IPRT/IPLT = 0 e
25.
CMMM DO NOT PLOT: STEAM, CLAD THICKHESS.H2 GENERATION GRAPHS IF l
26.
C ISTM,IZROX,IH2 = 0 e
27.
CMMM PLOTTING MODE l
28.
C MODE : O LINES AND POINT e
29.
C
. MODE : 1 POINTS ONLY l
30.
C MODE : 2 LIHES ONLY
.31 IPRT.: 1 32.
IPLT.: 1 33.
ISTM = 0 8
54.
MODE : 0-l 35.
IZROX: 0 36.
IH2 = 0 l
37.
ZZZ = 0 s
37.1 H2 GEN : 0.
.l 38.
CMMMM INCREMENTATION INIZITIALIZATION 4
39.
C DELX : STEP INCREMEHT (FT) 40.
C DTIME: TIME INCREMENT (HRS) e 41 C
ENDTME : (DEFAULT) EHD TIME OF SCEHERIO (HRS) 42.
C ITSTEP = (DEFAULT) HUMBER OF STEPS l
~43.
DELX : 1./12.
PNJ j
44.
DTIME: 44./3600.
rgy 44.1 DTIMET = DTIME pgy 45.
ENDTME : 1 WD" 7
45.
ITSTEP = ENDTME/DTIME +.1 47.
CMMMM IF METHOD : 0 PROGRAM WILL CALCULATE WATER LEVEL BASED OH l
48.
CMMMM PRESSURE, WATER FROM RCS COLD LEG FLOWING BACK PNJ AFTER RAISING WATER LEVEL IH RCS OTSG SIDE 1FT, sa t
49.
CMMMM 50.
CMMMM AND BLOCK VALVE POSITION cy) 51 CMMMM IF METHOD : 2 WATER LEVEL AS A FUNCTIDH OF TIME IS DETERMINED BY 52.
CMMMM THE FUNCTIDH 'ALEVEL'. THE PRESSURE IS READ IN AS A 53.
C OF TIME IF OPTION : 1 IS SELECTED
~ $
-54.
METHOD = 2 55.
OPTION : 1 56.
C 57.
CMMMM DATA IMPUT 4
a 58.
C METHOD 0 59.
IF(METHOD.NE.0) GO TO 50 60.
C READ IN PRESSURE, RCS COLD LEG TEMPERATURE, 61.
C BLOCK VALVE POSITION AS FUNCTIONS OF TIME SINCE 62.
C UNCOVERING THE CORE.
FIRST HUMBER SHOULD BE THE 63.
C HUMBER OF ORDERED PAIRS THAT FOLLOW FOR THAT PARAMETER.
64.
C IBLOCK : 0 BLOCK VALVE CLOSED 65.
C IBLOCK : 1 BLOCK VALVE OPEN 66.
READ (5,M) IDIVP 67.
READ (5,M) (PRESCI),PTIME(I),I:1,IDIVP) 68.
READ (5,M) IDIVT 69.
READ (5,M)(SGT(I),STIME(I),I:1,iDIVT) 70.
READ (5,M) IDIVB 71.
READ (5.M)(IEMOV(I),BTIME(I),I: 1,IDIVB)
'72.
C DETERMINE THE LIMITING TIME FOR THE SCEHARIO 73.
ENDTME = PTIME(IDIVP) 74.
IFCENDTME.GT.STIMEfIDIVT))ENDTME:STIME(IDIVT) 75.
IF(ENDTME.GT.BTIMECIDIVB))ENDTME:BTIME(IDIVB) 76.
ITSTEP = ENDTME/DTIME
-77.
C METHOD 1 78.,
50 IF((METHOD.NE.2).OR.(OPTION.NE.1.)) GO TO 60 79.
READ (5 M) IDIVP 79.1 DD 52 I:1,IDIVP 30.
READC5,M) PRESCI),PTIME(I) 1 80.1 52 CONTINUE j (81.
ENDTME = PTIME(IDIVP) i 82.
ITSTEP ENDTME/DTIME
(
83.
60 CONTINUE 84.
CMMMM INITIALIZE OTHER DATA PARAMETERS l
85.
CMMM. GEOMETRIC PARAMETERS i
86.
C ROF : RADIUS OF FUEL (FT)
THC CLADDING THICKHESS (FT) j 87.
C ROR = RADIUS OF ROD (FT)
ASG : X-AREA 0F STEAM GENERATORS (SQFT) 88.
C ACORE : AREA 0F CORE (SQFT) AS : AREA 0F STEAM FLOW PER ROD (SQFT)
'89.
C HEIGHT : CORE WATER VOLUME /X-SECTION AREA l
90.
C TMR : TEMP MEAN ROD TMS : TEMP MEAN 3 TEAM i
91 C
SGT = STEAM GENERATOR (SIDE) T EMP l
.92.
ROF.:.185/12.
.93.
.0265/12.
94.1 ROR :.215/12.
l 9 5. -
ASG ZZZ l
96.-
ACORE : ZZZ-97..
AS : 1.23E-3
- 98.,
HEIGHT : ZZZ
! s99.
PIE = 3.14159 l
99.1 RIC : ROR-THC 99.2 DENSF : 647.
8 99.3 DENSC = 406.
s99.4 AVDENS : PIEM(CRORNM2-RICMW2)MDENSC+ROFMM2NDENSF)
~ 100.
CMMM DETERMINE HODE POINTS AT 1 FT INTERVALS rs)
! 1 G 1. i H : INTL 1./DELX + 0.1) ps) 102.,
H12 : HM12 N
103.-
H0DEC1) =1 J""
104.
DO 1 I:2,13 105.,
NODECI) = (I-1)MN 4
106.
1 CONTINUE rs)
, 107.1,*
CMMM INITIALIZE POWER PARAMETERS
-a 103.
C RPF : RADIAL PEAKING FACTOR DHF = DECAY HEAT FACTOR sg) 109.-
C RTIME : REAL TIME SINCE UNCOVERING (HOURS) l 110..
C APFBCXi,X2) : INTEGRAL-AVERAGED AXIAL PEAKING FACTOR 111.4 RPF 1.467 1
a 112.,
DO 2 I:1,H12 113.
X1 = FLOAT (I-1)MDELX 114.
X2 : FLOAT (I)MDELX 115.
APF(I) : APFB(X1,X2) 1 16.,.
X0ICI) = 1.E-6 1 117.
2 CONTINUE i 118.
PBAR = 6.105M3412.9
> 119. J CMMMM MISC IHITIALIZATIDHS l 120.
C DRIP: NET LBS WATER ADDED TO RCS COLD LEG SIDE SINCE BLOCK 121.
C VALVE CLOSES
} 122.
DRIP : 0 l
123.-
C SGV : VOLUME REQUIRED TO CAUSE WATER DRIP INTO REACTOR
} 124. /
SGV = ASG M 1,
125.
C MARK : CURREHT HDDE POINT AT WATER INTERFACE 126.
MARK : 0
- 127.,
C DROP = AMOUNT OF SPILL OVER FROM RCS COLD LEG SIDE i28..'
DROP = 0 1
129.
C IWARN : CUMULATIVE HUMBER OF HODES OVER ONE THAT THE l 130..
C CORE LEVEL DROPS / RISES TO IN 1 TIME STEP.
131. /
IWARN : 0 C
OUTPUT COUNTERS
's f.
132.,
133.8 M2 : (10./60.)/DTIME 134..
M3 : M2 i
135.,
MPRT = 6 1
( 136.
INUM : 1 i 137.c HUHOLD : 0 138..
MDIST = 0 5
139.;
TMAX : 0 MINTME = ENDTMEM60.
140...
141.c
'C WATER IN CORE IHITIALLY
! 141.1 RTIME : 0.
-l 142.
CALL PROPRT(DHF,TSAT,HFG,RHOW IBLOCK,IDRIP,0.)
8 143.
C IDRIP = 1 DRIP BACK OCCURING l 144.
C IDRIP = 0 HD DRIP BACK LBSW = ACORENHEIGHTMRHOW i 145.
i l 146 C
TEMPERATURE PROFILES
+ 147.
DO 3 I:1,N12 6
l 148.
TMR(I) : TSAT 149.
- 150.
ECHCI) : FLOAT (I)MDELX l 150.1 ZRGEN(I):0.
' 151 3 CONTINUE l 152.
CMMMM MAIN i 153.
DD 100 I:1,ITSTEP l 154.
RTIME = FLOAT (I)MDTIME 155.
ECT(I) : RTIMEM60.
l 156.1 CH2(I) : D.
t 137.
CALL PROPRT(DHF,TSAT,HFG,RHOW,IBLOCK,IDRIP,RTIME)
" 153.
CMMM HEIGHT CALCULATION rs) 159.
CMM CALCULATE MASS FLOW RATE, MDOT, LBS/ HRS ps) 160.
CM CALCULATE ENERGY GENERATED UNDER WATER ps)
,, 151 POW.: RPFMPBARMDHF 4*"
162.
HT = FLOAT (MARK)MDELX 163.
TPOW:POWMAPFB(HT,12.)M(12.-HT) 164.
C ADD OR SUBTRACT EHERGY TO SET RODS AND WATER AT CURRENT TSAT rs)
L, 165.
SE : 0.
CX) 166.8 M = MARK + 1 c;)
167.
i DO 4:J:M,H12 i 168.
SE : CPRDT(TMR(J),TSAT) + SE TMR(J),= TSAT*
1S9.
Q
e 170.
TMS(J) : TSAT 171 TDELT(J) : TSATM2.
172.
4 CONTINUE 173.
C 174.
WSE : 0 175.
IF(METHOD.EQ.0)WSE : FLOAT (IDRIPM(1-IBLLCK))MDROPM l 176.
XCPWDT(SGTCRTIME),TSAT) + LBWS M CPWDT(TMS(J),TSAT) 177.
HPOW = TPOW - SE - WSE 178.
MDOT = NPOW/HFG t
179.
C l 180.3 IF(METHOD.NE.0) GD TD 70 131 DROP = MDOT M DTIME M FLOAT (1-IBLOCK) f 182.
DRIP = DRIP + DROPM FLOAT (1-IDRIP)
, 183.
CMM CALCULATE HEIGHT 184.
LBSW = LBSW - MDOTMFLOAT(1-IDRIP)MDTIME i 185.
MARK 2 : (HEIGHT - LBSW/(RHOWMACORE))/DELX + 0.49 8
186.
70 IF(METHOD.EQ.2) MARK 2 : ALEVEL(RTIME)/DELX +.49 l 186.1 IF(I.EQ.1.AND. MARK 2.LT.1) MARK 2 : 1 187.i CMMMM CALCULATE FUEL / STEAM TEMPERATURES l
188..
CMMM DETERMINE EXTENT CORE MOVED i 189.
IHOLD 0
's 190.
IF(MARK 2.EQ. MARK) IHOLD : 1 190.2 IF(MARK 2.GE. MARK) GO TO 71 190.4 M1 : MARK 2 + 1
! 190.5 DO 74 J:M1,H12 i 19C.6 TMR(J) : TSAT l 190.7 TMS(J) : TSAT
- 190.8 74 TDELT(J) :2.MTSAT l 190.9 71 CONTIHUE 191 IWARN : IABS(MARK-MARK 2) + (IHOLD - 1) + IWARN l 192.
HUHOLD :IHOLDM(IHOLD+HUHOLD) 193.
MARK = MARK 2 i
l 1?4.
IF(MDIST.LT. MARK) MDIST = MARK i 195.
DO 5 K:1, MARK
- 196.
J = MARK - K + 1 197.
CALL PROPTE(CPR, CPS,MUS,RHOS,KS,TMR(J),TMS(J),RTIME) l 198.
22 2
199.
IF(CIHOLD.EQ.1).0R.(J.NE. MARK)) Z2 : 1
' 200.
CMMM CALCULATE THE HEAT TRANSFER COEFFICENT 200.1 TRR : TMR(J) + 459.7
- 200.2 TRS : TMS(J) + 459.7 200.24 DELTT ABS (TRR-TRS) e 200.25 IF(DELTT.EQ.0.) GO TO 106 l 200.4 HRAD :.3942E-9M(TRRMh4-TRSMM4)/(TRR-TRS) 200.45 GO TO 107 8
200.46 106 HRAD : 0.
$ 201 107 M = HTC(ZZZ) + HRAD 202.
T MDOTMCPSMDTIME/DELX/2.
ps) 203.
204.
BR : AVDENSMCPR IN) 205.
C: PIEMRORMHMDTIME/Z2 PN)
} 206.
D::'CM(TMR(J)-TMS(J))
J2=
207.
i 208.
TA = C + BS + E ps)
? 2 0 9. ' t-TB :.D - F + BSMTMSCJ)
C33 ATMS : T1S(J) 213.
% 210.38-CMMMM KMELT IS FLAG INDICATING CLAD MELT.
IF IT'S 1 NO OXID HEAT ADDED.
210.1 IF(KMELTCJ).EQ.1) GO TO 151
- 212.
150 A = APF(J)MPOWMDTIME/Z2 +ZRGEHCJ)MDTIME/Z2
.CA+ERMTMR(J)-D)MTA+TBMC)/((BR+C)MTA-CMM2) 213.
152 TTMR2 : (
i
e
. 214.
IF(TTMR2.LT.3600.) GO TO 153 214.01 DTIME : (3600.-TMR(J))MDTIME/(TTMR2-TMR(J))
214.02 CMMMM NODE HAS EXCEEDED CLAD MELT TEMP OF 3600 DEG F.
214.1 TTMR2 = 3600.
214.2 KMELT(J):1 j 219.
153 CALL ZROX(TMR(J),TTMR2,X0I(J),ZRGEN(J),H2 GEN,KMELT(J))
219.5 DTIME DTIMET
! 220.
X0I(J) : XOF 221.
GO TO 160 221.1 151 A = APF(J)MPOWMDTIME/Z2
, 221.2 TTMR2:((A+BRMTMR(J)-D)MTA+TBMC)/((BR+C)MTA-CMM2) 221.3 H2 GEN:0.
222.
160 CONTINUE i
8 223.
THR(J) : TTMR2 l 224.
IF(TMR(J).GT.TMAX) TMAX:TMR(J) 225.
TMS(J) : (CMTMR(J)+TB)/TA 226.
TDELT(J) : TMS(J) + ATMS 229.
CH2(I):H2GEMMDELXM.30481 + CH2(I) 230.
5 CONTIHUE
- 230.1 TMDOT:MDOTM25.22NDTIME j 230.11 DELSTM:TMDOT-CH2(I)
's 230.2 IFCCTMDOT-CH2(I)).LT.O.) WRITEC6,701) TMDOT,CH2(I) 230.3 701 FORMAT (/2X,16HSTEAM STARVATIOH,1X,2F8.3) 231 C
SUM CURRENT H2 GEN WITH PAST H2 GEN iI 232.
IFCI.NE.1)CH2(I) : CH2(I) + CH2(I-1) l 233.
CMMMM DATA COLLECTION FOR DUTPUT 234.
CMMM PRINTING l 235.
IF(IPRT.EQ.0) GO TO 170 236.
C PRINT DATA AFTER EVERY SIX TIME STEPS 237.
. X5 : NUHOLD/6 - FLOAT (HUHOLD)/6.
e 238.
IF(NUHOLD.EQ.0) X5:1 l 239.
IF((MPRT.NE.6).AND.(X5.NE.O.)) GO TO 170 240.
WRITE (6,700) e 241 700 FORMATC/,2X 4HNODE 6X,14HCORE HEIGHT-FT,7X,8HTIME-MIN, 242.
X7X,10HFUEL DEG-F 6X,11HSTEAM DEG-F,4X,16HFLOW RATE-LB/ HRS, 243.
X2X,10HZR TH-MILS,5X,14H0XID-HT-FRACTN) 244.
DO 702 J:1, MARK 245.
ZRTH:(THC-2./3.MX0ICJ)/.30481)M12.E3
+
245.1 IF(X0I(J).GT.1.E5) ZRTH:0.
- 245.3 FRACTH.: ZRGEN(J)/ POW 246.
WRITE (6,710) J,ECH(J),ECT(I),TMR(J),TMS(J),MDOT,ZRTH,FRACTH 247.
710 FORMAT (2X,I3,6(10X,F7.2),8X,F7.2) 248.
702 CONTINUE 243.1 WRITE (6,711) TMDOT,DELSTM 248.2 711 FORMAT (4X,16HSTEAM PRODUCED :,F5.2,2X,15HSTEAM SURPLUS :,F5.2.
l 248.3 XIX 5HMOLES)
IN)
' 250.
MPRT : 0 PN) 251.
170 CONTINUE rs) f251.1 MPRT1: MPRT + 1 43, 3 252.
CMMM PLOTTING 253.
IF(IPLT.EQ.0) GO TO 189
$ 254.
CMM HISTORIES PN) t 255.
DO 180 J:1,13 CX3 256.
M = NODECJ) ps) 257.
- - TRCJ.I) : TMR(M)
IF(ISTM.HE.0) TS(J,I) : TMS(M) 258.
IFCIZROX.EQ.0) GO TO 180 260.
ZRTH,: (THC-2./3.MX0I(M)/.30481)M12.E3 IF(X0I(J).GT.1.E5) ZRTH:0.
260.1 ~
ZR(J,I) : ZRTH 261..
e
e 262.
180 CONTINUE 263.
Wl C'.*EL C I) = 12. - DELXMFLOAT(MARK)
- 264, 189 CONTINUE 265.
CMM PROFILES 266.
IF(I.NE.M2) 30 TO 199 I 267.
DO 190 J:1,H12
' 268.
TPCINUM,J) : TMR(J) i 269.
IFCISTM.NE.0) TPSCINUM,J) :TMS(J)
) 270.
190 CONTINUE
- 271.
M2 : M2 + M3
- 272.
IHUM = INUM + 1
- 273.
. 199 CONTINUE i 274, 100 CONTIHUE
- 275.
C i 276.
CMMMM PLOTTING OUTPUT 277.
IFCIPLT.EQ.0) GO TO 900 278.
CFMM DO NOT DRAW GRID LINES UNLESS IGRID : 1
>! 279.
CMMM HPLOT VARIABLES (XARAY,YARY,HPTS,XMIN,XMAX,YMIN.YMAX, 280.
C TITLETOP.TITLESIDE,TITLEBOT, MODE,IGRID) t 281.
YMIN = 0.
l 282.
YMAX : F'0AT(INT (TMAX/1E3)+1)M1E3
- 283.
MMODE : MDIST/N l 284.
DO 8S0 I: 1 FHODE l 285.
DO 840 J:1,ITSTEP 286.
YARYCJ) : TR(I,J) l 287 t 840 CONTINUE l 288.
L: I e 289.
IF(I.GT.10) L = I-10 290.
CALL DSPECS(' SYMBOL', CHAR (L))
e 291.
CALL NPLOT(ECT,YARY,ITSTEP,0.,MINTME,YMIH,YMAX, l 292.
X'QFUEL TEMPERATURE HISTORIES OF 1 FT NODESQ',
, 293.
X'QTEMPERATURE - DEG - FQ','QTIME - MINUTESQ', MODE,I) i 294.
850 CONTINUE I 295.
CALL PP ADVH j 296.
HUMP = MINTME/10.
297.
DO 851 I:1,NUMP i 298.
DO 841 J:1,ITSTEP l 299.
YARYCJ) : TP(I,J) i 300.
841 CONTINUE j 301
.L>
I+1 302.
IF(L.GT.10) L=I-9 1
303.
CALL DSPECS(' SYMBOL', CHAR (L))
l 304.
CALL HPLOT(ECH,YARY,H12,0.,12.,YMIN,YMAX, 8 305.
fX'QFUEL PROFILE -- 10 MINUTE INTERVALSQ',
j 306.
.X'QTEMPERATURE - DEG - FQ','QHEIGHT FROM TOP OF CORE - FTQ',
IN3 307.
XMODE,I)
.' 308.
851 CONTINUE IN) 309.
CALL PP ADVH rs) f 310.
CALL DSPECS(' SYMBOL','N')
Jd.
l 311 CALL HPLOT(ECT,WLEVEL,ITSTEP,0.,MINTME,0.,12.,
X'QWATER LEVEL VS. TIMEQ', QWATER LEVEL - FTQ',
ps)
X'QTIME -- MINUTESQ', MODE,'1) 312.
- 313.
C33 CALL PP ADVN 314.
315.
IF(ISTM.EQ.0) GO TO 859 L/4 t
D0~853 I:1,MHODE i 316.
DO 843 J: 1,ITSTEP 317.
! 318.,
.o YARYCJ) : TSCI,J) 319.
- 843. CONTINUE 320..
4.
.L.: I
- 321 IF(L.GT.10) L: I -10
- 322.
. CALL DSPECS(' SYMBOL', CHAR (L))
323.
CALL HPLOT(ECT,YARY,ITSTEP,0.,MINTME,YMIN,YMAX, 324.
X'QSTEAM TEMPERATURE HISTORIES OF 1 FT HDDESQ',
325.
X'QTEMPERATURE - DEG - FQ','QTIME - MINUTESQ', MODE,I) 326.
853 CONTIhuE 327.
CALL PP ADVH 328.
DO 854 I: 1, HUMP 329.
DO 844 J:1,ITSTEP
'. 330.
YARY(J) : TPSCI,J) 331.
844 CONTINUE 332.
L=I+1 333.
IF(L.GT.10) L=I-9 334.
CALL DSPECS(' SYMBOL', CHAR (L))
335.
CALL HPLOT(ECH,YARY,H12,0.,12.,YMIH,YMAX, 336.
X'QSTEAM PROFILE -- 10 MINUTE INTERVALSQ',
337 X'QTEMPERATURE - DEG - FQ','QHEIGHT FROM TOP OF CORE - FTQ',
3~d.
XMODE,I) 339.
854 CONTINUE 340.
CALL PP ADVH
?} 341, 859 CONTINUE
- 342.
IF(IZROX.EQ.0) GO TO 8(b
] 343.
DO 855 I:1,MHODE b 344.
DO 845 J:1,ITSTEP
{ ', 345.
YARY(J) : ZRCI,J)
,. 346.
845 COHTINUE 347.
L=I 348.
IF(L.GT.10) L = I -an 349.
CALL DSPECS(' SYMBOL', CHAR (L))
.350.
CALL NPLOT(ECT,YARY,ITSTEP,0..MINTME,0.,THC,
' 351 X'QCLADDING THICKHESS HISTORIES OF 1 FT HODESQ',
l 352.
X'QCLADDING THICKHESS - MILSQ','QEXPOSED CORE HEIGHT - FTQ',
353.
XMODE,I).
,' 354.
855 CONTINUE 355.
CALL PP ADVH l 356.
860 CONTINUE a 357.
IFCIH2.EQ.0) GO TO 900 l 358.
CALL DSPECSC' SYMBOL','M')
4 359.
CALL NPLOT(ECT,CH2,ITSTEP,0. MINTME,0.,0.,
- 360.
X'QCUhdLATIVE HYDROGEH GENERATI0HQ',
361 X'QTOTAL HYDROGEN GENERATED - MOLESQ',
- 362.
X'QTIME -- MINUTESQ', MODE, 1) 363.
CALL PP ADVN 364.
900 WRITE (6,901) CH2(ITSTEP),IWARN
'. 365.
901 FORMAT (10X,26HTOTAL HYDROGEN GEHERATED =,E10.4,2X,5HMOLES, 366.
X10X,7HIWARN
,IS)
+
367.
CALL PP CLOS rN) 3 368.
STOP.
pg) 369.
EHD I\\3 370.
FUNCTION AVE (X,Y,HPTS,X1) 371 CMMMM FUNCTION CALCULATES THE IHTERPOLATED VALUE OF THE Y 45*
372.
C ARRAY GIVEN A VALUE Ih THE X ARRAY. NPTS : HUMBER OF 373.
C POINTS IN EITHER ARRAY.
INJ 374.
DIMENSIDH XC600), YC600)
CX3 375.
I: 0 43, 376.
1 I: I+ 1 377.. -
IF((I.GT.HPTS).0R.(HPTS.GT.600)) GO TO 4 378.
IF(X(I).LT.X1) GO TO 1 379.
IFCI.NE.1) GO TO 2 380.
AVE : YC1)
RETURN 381.
4
e
- 383.
2-AX = X(I-1) 384.
AY : Y(I-1) 385.
3 Y1 : Y(I) - ((X(I)-X1)/(X(I)-AX))M(Y(I)-AY) 386.
AVE : Y1 387.
RETURH 388.
4 WRITE (6,5) I, HPTS,X1 389.
5 FORMAT (5X,9HERROR AVE,5X,3HI :I3,5X,6HHPTS =,I3,5X,
- 390.
X4HX1
,E10.4) 391.
STOP
=
392.
EHD r 393.
SUBROUTINE PROPRT(DHF TSAT,HFG,FFLW,IBLOCK,IDRIP,RTIME) 394.
DIMENSIDH PRES (60),SGT(60),IEMGt(60),PTIME(60),STIME(60),
395.
XBTIME(60)
- 396.
COMMON /COMRT/ PRES,SGT,IEMOV,PTIME,STIME.BTIME, METHOD,0PTION,IDIVP 397.
DHF : 0.011 398.
IF(OPTION.HE.1) GO TO 1 399.
P: AVE (PTIME, PRES,IDIVP,RTIME)
- 400.
HFG = 8.43895E2-(1.91536E-1)MP l 401.
TSAT = 1.16808E2MPMM(0.222885) 404.
IF(METHOD.EQ 0) IBLOCK : AMID(IEMOV,BTIME,HPTS.RTIME) j 404.1 RHOW = 0.
[ 404.2 IBLOCK 0.
404'3 IDRIP = 0.
i 404.4 RETURN
' 405.
CMMMM DEFAULT VALUES
'! 406.
1 CONTINUE 407.
TSAT = 560.
l 408.
HFG : 669.
40.9.
RHOW = 0 I 411 IBLOCK : 0 f 412.
IDRIP = 0 i 413.
RETURH e 414.
END SUBROUTINE PROPTE(CPR, CPS,MUS,RHOS,KS,TR,TS,RTIME) l 415.
DIMENSION PRES (60),SGT(60),IEMOV(60),PTIME(60),STIME(60),
416.
l 417.
XBTIME(60) i 418.
COMM0H/COMRT/ PRES,5GT,IEMOV,PTIME,STIME,BTIMF.!iETHOD,0PTION,IDIVP
! 449.
COMMON /COMZR/ROR,DTIME,THC,XOF 4'19.1 COMM0H/C0ZR/DENSF,DENSC,RIC,ROF
! 419.2 DATA CK1,CK2,CK3,TH,ED,RR/296.7,2.9JE-2,8.745E7,535.285,
! 419.3 X1.577ES,8.3143/
' 419.6 CMMMM COMPUTATION OF ROD AVERAGED SPECIFIC HEAT 419.7 CMMMM COMPUTATION OF FUEL SPECIFIC HEAT
$ 419.8 TK : 273.15+(5./9.)M(TR-32.)
419.9 CPF : (CCK1M(THMM2)MEXP(TH/TK))/(CTFMM2)M(EXP(TH/TK)-1)MM2) l 420.
X+CK2MTK+CK3MEDMEXP(-ED/CRRMTK))/(RRhTKNM2))/4.184E3 pg) 420.1 CMMMM COMPUTATION OF CLAD SPECIFIC HEAT
,' 420.2 IF(TK.LE.1090.) GO TO 2 INJ f 420.3 IF(TK.GE.1248.) GO TO 3 PN) 1 420.4 IF(TK.LT.1173.) GO TO 4 Jd=
420.5 CPC = 816.-6.133MCTK-1173.)
420.6 GO TO' 6 ps) 420'.8 2 CPC =.11899M(TK-3b3.)+281.
C%3 420.9 GO.TO 6 3 CPC = 356.
( 71 s 421.. -
421.1 GO TO 6
? 421.2*
4 CPC' : 3.925M(TK-1093.)+502.
421.3 6 CPC = c?C/4184.
421.4 CMMMM COMPUTATION OF AVERAGE SPECIFIC HEAT 421.5 CPR': ((RORNM2-RICMM2)MDENSCMCPC+ROFMM2NDENSFMCPF)/
g
a 421.7 X(CRORNM2-RICMM2)MDENSC+ROFMW2MDENSF) 421.8 CMMMM COMPUTATION OF STEAM DENSITY i 421.9 IFCOPTION.EQ.0) GO TO 7 422.
P = AVECPTIME, PRES,IDIVP,RTIME) 422.1 RHOS : 1./(C2.12736E-2)MEXP((-2.27353E-3)MP)M 2
422.2 XTSMM((6.86394E-1)M(EXP((2.23061E-4)MP))))
422.3 CMMMM COMPUTATION OF STEAM SPECIFIC HEAT 422.31 CMMMM CALCS USE CORRELATION OF RIVARD AND TORREY LASL LA-6104-MS 1975.
422.33 P = PM6.897E4 i 422.34 CMMMM P IS HOW IN DYHES/CMMM2 - CALC. OF* SAT TEMP IN DEG K (TST) 422.35 TST = 117.8M(PM1.E-6)MM.223 + 255.2 i 422.36 CMMMM CALC OF SAT SP HEAT, CSAT, IN DYNES-CM/GM/K -- R IS GAS CONST 422.37 CSAT = (1.-TST/647.3)MM(.8566)M9.5875E6 422.38 R = 4.6189E6 422.39 GAM = 1.30 422.4 CON : 2.M(GAM-1.)/(GAMMR) 422.42 ALP = (RMTST)MM2/(4.MP)M(1.-1./(CSATMC0H-1.)MM2) 422.43 TKS : 273.15 + 5./9.MCTS-32.)
422.44 CPS : 1./CONMC1. + RWTKSM((RMTKS)MM2-4.MALPMP)MM(.5))
l 422.47 CPS : 2.39132E-8 MCPS 7 422.6 MUS : 0
'a l 422.7 KS : O e 422.8 RETURN
' 422.9 1 CONTINUE l 423.
CMMMM DEFAULT AVERAGE VALUES FOR WATER AND STEAM PROP.
7 RHOS : 2.04 l 423.2 423.3 CPS :.52
' 423.5 MUS : 0 423.6 KS : 0 i 423.7
.RETURH
,' 423.8 END 426.
CMMMM SUBROUTIHE WT0X CALCULATES THE OXYGEN WEIGHT i
l 427.
C GAIH'0F ZIRCALOY OVER AN ASSUMED LINEAR 428.
C TEMPERATURE RAMP OF 1-DEG-K INCREMENTS l 429..
C WI : IHITIAL WEIGHT GAIH KG/MMM2 6 430.
C DT = TIME INCREMENT SECONDS 431 C
T1,T2 : INITIAL /FINAI TEMPERATURE - DEG F l 432.
SUBROUTINE WT0X(WI,T1,T2,DT,DELWT,W1) 435.
DATA A,B/16.80,2.007E4/
! 434.
W=0
' 434.1 DELWT = 0.
I 435.
TK1 = 273.15 + 5./9.M(T1-32.)
8 436.
TK2 = 273.15 + 5./9.M(T2-32.)
! 437.
WII:WI 438.
H: 1 439.
MSTEP:DTM3600.+.01 INJ 439.1 IF(MSTEP.LT.1) MSTEP = 1 Ps)
, 440.
HSTEP:HMMSTEP rsj 441 FLM:MSTEP a3, 442.
FLH:NSTEP 443.
SLOPE:(TK2-TK1)/FLM 444.
DO 1.I:1,HSTEP PN3
- 445.
AI=I-CX) 446.
T:TK1+SLOPEM(AI.5)MFLM/FLN C7%
447.
W:AMEXPC-B/T)MFLM/FLN/WII WII:WII + W 448.
L 448.1 -
DELWT:DELWT+W 449.
1 CONTINUE 450.
W1:WII 452.
900 RETURN i
a 453.
.END 454.
SUBROUTINE ZROX(T1,T2,X0I,ZRGEH,H2GEH,K) 455.
CMMMM ZROX CALCULATES THE POWER GENERATED (BTU /FT-HRS) FROM 456.
C THE ZIRCALOY-WATER REACTION:
457.
C ZR + 2H2O : ZR02 + 2H2 458.
C OVER A GIVEN TEMPERATURE RAMP. IT ALSO CALCULATES THE 459.
C MOLES OF HYDROGEN GENERATLD OVER THAT NODE.
i
- 460.
COMMON /COMZR/ROR,DT,THC,XOF 6 460.1 IF(X01.GT.1.01E5) GO TO 4
- 461 WI = X0IM5820.MO.26 I
CALL WT0X(WI,T1,T2,DT,DELWT,W1)
I 461.1 XOF : W1/(5820.M.26) l 462.
462.2 DELWT:DELWT/(5820.M.26) a 462.4 IFCK.EQ.1) GO TO 1 j 463.
CHECK :THC - 2./3.MX0F/.30481
! 464.
CMMM PRINT WARNIHG AND HALT PROGRAM IF CLADDING THICKHESS
{
j 465.
C IS EXCEEDED IH.0XIDATION
- 466.
IF(CHECK.GE.0.) GO TO 2 8 466.1 XOF = 3./2.MTHCM.30481 1 466.2 GO TO 2 467.
4 ZRGEN:0.
4 468.
X0F:1.E6 469.
H2GEH:0.
469.1 RETURN 470.
2 ZRGEN : 6490.M6.45E6M2.10M2.M(RORM.30481-l 471 X(X0F+X0I)/3.)MDELWT/(3600.MDT) 472.
C ZRGEN : WATTS / METER
- 473.
C ZRGEN WILL BE CHANGE TO BTU /FT-HR 47 4., -
C BY MULTIPLING BY AN APPROPIATE CONVERSIDH FACTOR i
476.
ZRGEN = ZRGEHM1.04028 I 47;.
CMMM CALCULATE THE MOLES OF HYDROGEN GENERATED j
4'S.
1 H2GEH:5.9604E5MDELWTM(.30481MROR-(X0F+X0I)/3.)
, 478.1 IFCCHECK.LT.O.) X0F:1.E6
- 480.
RETURN l 481.
END 482.
FUNCTION AMID(ARRAY 1, ARRAY 2,HPTS, VAL 2) l 483.
CMMMM AMID FINDS THE FIP.ST ELEMENT IN ARRAY 2 THAT IS HOT e 484.
C GREATER THAN VAL 2 AND RETURHS THE CORRESPONDING VALUE WARHING MESSAGE IS PRIHTED AHD THE 485.
C OF ARRAY 1.
, 486.
C PROGRAM HALTED IF THE DIMENSIDH OF EITHER ARRAY IS EXCEEDED.
l 487.
C HPTS : HUMBER OF POINTS IN EITHER ARRAY 488.
DIMEHSION ARRAY 1(60), ARRAY 2(60) 8 489.
I: 0 1 490.
1I=I+ 1 491 IF(CHPTS.GT.I).0R.(HPTS.GT.60)) GO TO 2 492.
IFCARRAY2(I).LT. VAL 2) GO TO 1 493.
AMID = ARRAY 1(I) psy 4
494.
RETURN I\\3
" 495.
2 WRITE (6,3) I,HPTS, VAL 2
! 496.
3 FORMAT (5X,10HERROR AMID,5X,3HI : 13,5X,6HHPTS :,I3, PN)
I 497.
X5X,6HVAL2 :,F7.2) 42=
} 498.
STOP j 499.
END ps)
FUNCTION ALEVELCRTIME) l 500.
CX) 500.01 CMMMM ALEVEL IS THE AMOUNT OF CORE UNCOVERED IN FEET 500.1'-
TMB 8./14.
- d 8
" 50'1 IF(RTIME.LT.TMB) ALEVEL = 14.MRTIME 502.
IFCRTIME.GE.TMB) ALEVEL = 8.
i 503.
RETURN 504.
END.
i 4
a r
l 505.
SUBROUTINE HPLOT (XARRAY,YARRAY,HPTS,XMIN,XMAX, i 506.
1YMIN,YMAX, TOP, SIDE. BOT, MODE,IGRID) 507.
DIMENSIDH XARRAY(1), YARRAYC1), TCPC1), SIDE (1), BOT (1) 508.
DIMENSIGH BUFX(500), BUFYC500), SPECS (30), GIVEH(5) 509.
C...
INITIALIZE THE SPECS ARRAY i 510.
CALL S SPECS (SPECS) 511 C...
PLACE THE PASSED PARAMETERS INTO THE SPECS ARRAY.
l 512.
SPECS (3):XMAX
- 513.
SPECS (4):XMIN 514.
SPECS (5):YMAX i 515.
SPECS (6):YMIN l 516.
SPECS (13): FLOAT (HPTS) 517.
XLOW:XMIN 518.
XUP:XMAX
- 519.
C...
IF XMAX IS GREATER THAN XMIH, THEN DO NOT SCALE THE X AXIS.
1 520.
IF (XUP.GT.XLOW) GO TO 300 521 XDIV:SPECSC9) 522.
IXSKIP: SPECS (14)
- 523.
XLOW:0.0 524.
IF (NPTS.GE.1) XLOW:XARRAYC1) l 525.
XUP:XLOW
's
- 526.
IFL(HPTS.LT.2) GO TO 200 I 527.
IX:1 528.
C...
SEARCH FOR MAXIMUM AND MINIMUM VALUES IN THE X ARRAY.
a l 529.
DO 10G J:2,HPTS
, 530.
IX:IX+IXSKIP l 531 XI:XARRAY(IX) s 532.
IF (XI.LT.XLOW) XLOW:XI
- 533.
IF (XI.GT.XUP) XUP:XI i 534.
100 CONTINUE
' 535.
200 IF (XUP.LE.XLOW) XUP:XLOW+1.0 536.
C...
SET UP Tile GIVEN ARRAY.
- 537.
GIVEN(1):XUP l 533.
GIVEN(2):XLOW 539.
GIVEN(3):XDIV 540., ;t C...
CHOOSE SCALING HUMBERS FOR THE X AXIS.
- 541 CALL F A B LI X (GIVEH, SPECS)
{.542.
i300 YLOW:YMIN
, 543.
YUP:YMAX j 544.
C...
IF YMAX IS GREATER THAH YMIH, THEN DO NOT SCALE THE Y AXIS.
1 545.
IF (YOP.GT YLOW) GO TO 600
' 546.
YDIV: SPECS (10)
! 547.
IYSKIP: SPECS: 15) 543.
YLOW:0.0 549.
IF CHPTS.GE.1) YLOW:YARRAY(1)
I 550.
YUP =YLOW 551 IF (HPTS.LT.2) GO TO 500 552.
IY:1 7 553.
C...
SEARCH FOR MAXIMUM AND MINIMUM VALUES IN THE Y ARRAY.
i 554.
DO 400 J:2,HPTS rs) 6 555.
IY:IY+IYSKIP psj 556.
YI:YARRAY(IY) pg) 557.
IF.(YI.LT.YLOW) YLOW:YI I 553.
IF (YI.GT. YUP) YUP:YI J**
559.
400 CONTINUE 500 TF (YUP.LE.YLOW) YUP:YLOW+1.0 rs)
. 560.
- C 561.
C...
BET UP GIVEN ARRAY.
CX3 562.
GIVEHC1): YUP CX3 563.
GIVEH(2):YLOW 564.
GIVEN(3):YDIV
' f4
e 565.
C...
. CHOOSE SCALING HUMBERS FOR THE Y AXIS.
1 566.
CALL F A B LI Y (GIVEH, SPECS) 567.
C...
DRAW THE GRID LINES.
568.
600 IF(IGRID.EQ.1) CALL GD LI LI (SPECS) 569.
C...
DRAW ANHOTATION HUMBERS ALONG THE X AXIS.
3
~
570.
IF(IGRID.EQ.1) CALL HO S LI B (SPECS) 571 C...
DRAW ANNOTATIDH HUMBERS ALOHG THE Y AXIS.
~,
572.
IFCIGRID.EQ.1) CALL H0 S LI L (SPECS) 573.
C...
PLOT SYMBOLS AT THE DATA POINTS.
574.
IF((MODE.EQ.0).0R.(MODE.EQ.1)) CALL PS LI LI (XARRAY 575.
1,YARRAY, SPECS) 576.
C...
CONNECT THE DATA POINTS WITH A SMOOTH LINE.
', 577.
IF ((MODE.EQ.0).0R.(MODE.EQ.2)) CALL PF LI LI (XARRAY 578.
1,YARRAY,BUFX,BUFY, SPECS)
- 579.
C...
DRAW HEADING ALOHG TOP OF PLOT.
580.
Ic(IGRID.EQ.1) CALL TITLE T (TOP, SPECS)
' 581 C...
DRAW TITLE ALONG Y AXIS.
l 582.
IF(IGRID.EQ.1) CALL TITLE L (SIDE, SPECS) 583.
C...
DRAW TI1LE ALOHG X AXIS.
! 584.
IFCIGRID.EQ.1) CALL TITLE B (BOT, SPECS)
RETURN l 585.
586.
END 4 587.
/N
// DATA EXEC IPPDLKGO l 588.
589.
//GO.FT05F001 DD M a 589.1 33 l 590.
1005.,0.
' 591 980.,.04167 l 592.
955.,.08333 8
593.
925.,. 125
.! 594.
900.,.16667 595.
875.,.20833 l 596.
850.
25
- 597.
825.,.29167
- 598.
800.,.33333 599.
780.. 375 600.
760.
41667 I 601 740.,.45833
- 602.
720.,.5
} 603, 700.,.54167
? 604.
680.,.58333
! 605, 670,,.625 l 606.
670,.66667
- l607, 680.,.70833 v
608.
690.,.75 rs;
- 609, 712.
79167 pg) 1! 610.
740.,.83333 d
='
- 611, 780.,.875
.f 612.
820.,.91667 1 613.
865.,.95833
'NJ 614.
907.,1.0 C33 j 614.1 955.,1.04167 sg) 614.2 1000.,1.08333 i 614.3 1055.,1.125 j 61464)1 P 1110.,1.16667
- 614.5 -
1180.,1.20833
'; 614.6 1250.,1.250 614.7 1325.,1.29167 1410.,1.33333
- 614.8 615.
/N e
617.
//FPLOT EXEC IPPDPRT 618.
//FPLOT EXEC IPPDCAL,PLTHAME:GPMBOILD 4
1 r
4 e
b t
1-t 6
e e
i
.f 9
9 8
e e
e G
e
?
k
+
e L:
6 i /
J' f
,1 e
e 19 a
e i
e 4
N N
4 e
N
.w m
O g
/ 4 *'
.o I'
o J
t 9
1 ?,
q
HODE CORE HEIGHT-FT TIME-MIN FUEL DEG-F STf4M DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH 1
0.08 0.73 580.56 6 A.55 6.15 26.47 0.00 2
0.17 0.73 564 65 544.42 6.15 26.47 0.00 STEAM PRODUCED = 1.89 STEAM SURPLUS : 1.89 MOLES NODE CORE HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH
.1 0.08 5.13 702.26 552.24 5.78 26.47 0.00 2
0.17 5...
709.25 551.23 5.78 26.47 0.00
.3 0.25 5.13 714.68 549.30 5.78 26.47 0.00 4
0.33
'5.13 717.63 547.93 5.78 26.47 0.00 5
0.42 5.13 718.82 547.42 5.78 26.47 0.00
,6 0.50 5.13 716.89 546.31 5.78 26.47 0.00 7.
0.58 5.13 712.94 544.34 5.78 26.47 0.00 8
0.67 5.13 705.06 542.99 5.78 26.47 0.00 9
0.75 5.13 694.90 542.62 5.78 26.47 0.00 10 0.83 5.13 679.80 541.73 5.78 26.47 0.00 11 0.92 5.13 662.13 540.05 5.78 26.47 0.00 12 1.00 5.13 638.32 539.09 5.78 26.47 0.00 13 1.08 5.13 ',
611.67 539.26 5.78 26.47 0.00 i
14 1.17 5.13 577.48 538.98 5.78 26.47 0.00 STEAM PRODUCED = 1.78 STEAM SURPLUS : 1.78 MOLES HODE CORE HEIGHT-FT-TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH 1,
0.08 9.53 757.09 592.80 5.22 26.47 0.00 2
0.17 9.53 770.83 591.13 5.22 26.47 0.00 i3 0.25 9.53 783.71 588.45 5.22 26.47 0.00 4
0.33 9.53 795.48 586.05 5.22 26.47 0.00 5
0.42 9.53 806.39 584.35 5.22 26.47 0.00 6
0.50 9.53 816.03 582.06 5.22 26.47 0.00 7
0.58 9.53 824.74 578.80 5.22 26.47 0.00 8
0.67 9.53 831.98 575.87 5.22 26.47 0.00 9
0.75 9.53 838.26 573.70 5.22 26.47 0.00 10 0.83 9.53 842.78 571.04 5.22 26.47 0.00 11 0.92 9.53 846.24 567.48 5.22 26.47 0.00 12 1.00 9.53 847.57 564.31 5.22 26.47 0.00 13 1.08 9.53 847.75 562.05 5.22 26.47 0.00 14 1.17 9.53 845.31 559.38 5.22 26.47 0.00 15 N
1.25 9.53 841.51 555.69 5.22 26.47 0.00 16 N
1.33 9.53 834.52 552.64 5.22 26.47 0.00 17 N
1.42 9.53 826.03 550.79 5.22 26.47 0.00 1.50 9.53 813.58 548.48 5.22 26.47 0.00 18 4
19 1.58 9.53 799.41 545.23 5.22 26.47 0.00 20 1.67 9.53 804.56 542.75 5.22 26.47 0.00 21 N
1.75 9.53 784.77 540.22 5.22 26.47 0.00 22 1.83 9.53 763.25 538.88 5.22 26.47 0.00 23 1.92 9.53 735.64 537.29 5.22 26.47
O.00 24 2.00 9.53 706.22 535.01 5.22 26.47 0.00 25 2.08 9.53 669.47 533.46 5.22 26.47 0.00 26 2.17 9.53 630.91 533.19 5.22 26.47 0.00 27-2.25 9.53 583.64 532.75 5.22 26.47 0.00 STEAM PRODUCED :-1.61 STEAM SURPLUS : 1.61 MOLES HODE CORE HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATF*iB/ HRS ZR TH-MILS OXID-HT-FRACTN 0.08 13.95 814.06 681.90 4.63 26.47 0.00 1
2 0.17 13.93 828.90 679.87 4.63 26.47 0.00 3
0.25 13.93 843.00 676.72 4.63 26.47 0.00 4
0.33 13.93 856.30 673.65 4.63 26.47 0.00 13.93 868.89 671.09 4.63 26.47 0.00 5
0.42
6 0.50 13.93 880.67 667.91 4.63 26.47 0.00 7
0.58 13.93 891.74 663.66 4.63 26.47 0.00 8
0.67 13.93 901.97 659.48 4.63 26.47 0.00 9
0.75 13.93 911.54 655.86 4.63 26.47 0.00 13 93 920.24 651.72 4.63 26.47 0.00 to 0.83 4
11 0.92 13.93 928.26 646.57 4.63 26.47 0.00 12 1.00 13.93 935.36 641.52 4.63 26.47 0.00 13 1.08 13.93 941.81 637.15 4.63 26.41 0.00 14 1.17 13.93 947.25 632.36 4.63 26.47 0.00 15 1.25 13.93 952.01 626.46 4.63 26.47 0.00 16 1.33 13.93 955.64 620.81 4.63 26.47 0.00 17 1.42 13.93 958.61 616.10 4.63 26.47 0.00 18 1.50 13.93 960.28 610.99 4.63 26.47 0.00 19 1.58 13.93 961.21 604.86 4.63 26.47 0.00 20 1.67 13.93 966.69 599.10 4.63 26.47 0.00 21 1.75 13.93 965.58 593.13 4.63 26.47 0.00 22 1.83 13.93 963.77 588.10 4.63 26.47 0.00 23 1.92 13.93 960.07 582.88 4.63 26.47 0.00 24 2.00 13.93 955.57 576.91 4.63 26.47 0.00 25 2.08 13.93 948.77 571.30 4.63 26.47 0.00 26 2.17 13.93 ',
941.10 566.74 4.63 26.47 0.00 27 2.25 13.93 930.58 562.11 4.63 26.47 0.00 28 2.33 13.93 919.08 556.82 4.63 26.47 0.00 29 2.42 13.93 904.05 552.04 4.63 26.47 0.00 30 2.50 13.93 887.96 548.47 4.63 26.47 0.00 31 2.58 13.03 867.55 544.89 4.63 26.47 0.00 32 2.67
- 13. 33 845.98 540.71 4.63 26.47 0.00 33 2.75 13.53 819.16 537.17 4.63 26.47 0.00 34 2.83 13.9S 791.17 534.99 4.63 26.47 0.00 35 2.92 13.93 756.89 532.81 4.63 26.47 0.00 36 3.00 13.93 721.47 530.05 4.63 26.47 0.00 37 3.08 13.93 678.64 528.04 4.63 26.47 0.00 38 3.17 13.93 634.79 527.46 4.63 26.47 0.00 39 3.25 13.93 582.28 526.89 4.63 26.47 0.00 STEAM PRODUCED : 1,43 STEAM SURPLUS : 1.43 MOLES H0DE CORE HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH 1
0.08 18.33 904.27 823.08 4.02 26.47 0.00 s2 0.17 18.33 918.29 821.26 4.02 26.47 0.00
'3 0.25 18.33 931.53 818.22 4.02 26.47 0.00 4
0.33 18.33 943.99 815.05 4.02 26.47 0.00 i5 0.42 18.33 955.73 812.24 4.02 26.47 0.00 6
0.50 18.33 966.72 808.75 4.02 26.47 0.00 7
0.58 18.33 976.99 804.09 4.02 26.47 0,00
'8 0.67 18.33 986.55 799.28 4.02 26.47 0.00 9
pg) 0.75 18.33 995.45 794.85 4.02 26.47 0.00 10 0.83 18.33 1003.66 789.85 4.02 26.47,'
0.00 pg) 11 0.92 18.33 1011. 2 783.74 4.02 26.47 O.00 2
12 I\\)
1.00 18.33 1018.11 777.49 4.02 26.47 0.00 13 Jh-1.08 18.33 1024.42 771.71 4.02 26.47 0.00 14 1.17 18.33 1030.66 765.47 4.02 26.47 0.00 15 rgj 1.25 18.33 1035.13 758.03 4.02 26.47 0.00 16 1.33 18.33 1039.55 750.57 4.02 26.47 0.00 sg) 17 1.42 18.33 1043.45 743.79 4.02 26.47 0.00 M5 I\\3 1.50 18.33 1046.70 736.61 4.02 26.47 0.00
'9 1.58 18.33 1049.43 728.32 4.02 26.47 0.00 1 21 1.67 18.33 1052.75 720.11 4.02 26.47 0.00 21 1.75 18.33 1054.35 711.53
'4.02 26.47 0.00 22 1.83 18.33 1055.49 703.59 4.02 26.47 0.00 23 1.92 18.33 1055.95 695.42 4.02 26.47 0.00 i
24 2.00 18.33 1055.95 686.38 4.02 26.47 0.00 25 2.08 18.33 1055.20 677.36 4.02 26.47 0.00 26 2.17 18.33 1054.03 669.07 4.02 26.47 0.00 l
27 2.25 18.33 1052.02 660.67 4.02 26.47 0.00 28 2.33 18.33 1049.56 651.49 4.02 26.47 0.00 i
29 2.42 18.33 1046.13 642.44 4.02 26.47 0.00 30 2.50 18.33 1042.27 634.26 4.02 26.47 0.00 31 2.58 18.33 1037.26 626.08 4.02 26.47 0.00 32 2.67 18.33 1Q31.75 617.22 4.02 26.47 0.00 t
33 2.75 18.33 1024.83 608.61 4.02 26.47 0.00 i
34 2.83 18.33 1017.43 601.05 4.02 26.47 0.00 35 2.92 18.33 1008.28 593.58 4.02 26.47 0.00 36 3.00 18.33 998.55 585.53 4.02 26.47 0.00 37 3.08 18.33 986.64 577.89 4.02 26.47 0.00 38 3.17 18.33 974.13 571.46 4.02 26.47 0.00 35 3.25 18.33 958.91 565.23 4.02 26.47 0.00 l
40 3.33 18.33 942.98 558.47 4.02 26.47 0.00 41 3.42 18.33 923.68 552.29 4.02 26.47 0.00 42 3.50 18.33 903.66 547.48 4.02 26.47 0.03 a
43 3.58 18.33 879.50 542.91 4.02 26.;*s7 0.00 l
44 3.67 18.33 's 854.54 537.84 4.02 26.47 0.00 45 3.75 18.33 824.59 533.46 4.02 26.47 0.00
{
46 3.83 18.33 793.87 530.59 4.02 26.47 0.00 47 3.92 18.33 757.17 527.92 4.02 26.41 0.00 8
48 4.00 18.33 719.72 524.73 4.02 26.47 0.00 e
49 4.08 18.33 675.24 522.31 4.02 26.47 0.00
?
50 4.17 18.33 630.09 521.48 4.02 26.47 0.00 l
51 4.25 18.33 576.69 520.80 4.02 26.47 0.00 STEAM PRODUCED = 1.24 STEAM SURPLUS : 1.24 MOLES HSDE CORE' HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH l
1 0.08 22.75 1045.00 101-8.60 3.39 26.47 0.00 2
- 0. 17 22.73 1057.54 1017.,82 3.39 26.47 0.00 3
0.25 22.73 1069.23 1015.72 3.39 26.47 0.00 e
4 0.33 22.73 1080.10 1013.31 3.39 26.47 0.00 5
0.42 22.73 1090.19 1011.10 3.39 26.47 0.00 I
6 0.50 22.73 1099.50 1008.13 3.39 26.47 0.00 7
0.58 22.73 1108.05 1003.88 3.39 26.47 0.00 l
8 0.67 22.73 1115. 6 999.28 3.39 26.47 0.00 8
9 0.75 22.73 1122.97 994.90 3.39 26.47 0.00 l
10 0.83 22.73 1129.38 989.85 3.39 26.47 0.00 e
11 0.92 22.73 1135.12 983.60 3.39 26.47 0.00 l
12 1.00 22.73 1140.21 977.01 3.39 26.47 0.00 i
13 1.08 22.73 1144.67 970.70 3.39 26.47 0.00 14 1.17 22.73 1148.52 963.86 3.39 26.47 0.00 f
15 1.25 22.73 1151.77 955.74 3.39 26.47 0.00 16 1.33 22.73 1154.44 947.36 3.39 26.47 '
0.00 17 1.42 22.73 1156.59 939.46 3.39 26.47 O.00
~
18 1.50 22.73 1158.18 931.11 3.39 26.47 0.00 19 1.58 22.73 1159,26 921.60 3.39 26.47 0.00 20 1,67 22.75 1160.05 911.94 3.39 26.47 0.00 21 Ps>1.75 22.73 1160.14 901.75 3.39 26.47 0.00 22 rsj i 83 22.75 1159. 0 891.98 3.39 26.47 0.00 8
23 1.92 22.75 1159.00 881.90 3.39 26.47 0.00 24
- g. )2.00 22.73 1157.77 870.88 3.39 26.47 0.00 d*'2.08 22.73 1156.11 859.63 3.39 26.47 0.00 25 26 2.17 22.73 1154.08 848.84 3.39 26.47 0.00 27 rNJ !.:25 22.73 1151.64 837.87 3.39 26.47 0.00 2E sg)i.33 22.73 1148.84 826.04 3.39 26.47 0.00 (ja.42 22.73 1145.53 814.05 3.39 26.47 0.00 2
29 i
a 30 2.50 22.73 1142.13 802.63 3.39 26.47 0.00 31 2.58 22.73 1138.22 791.12 3.39 26.47 0.00 32 2.67 22.73 1134.01 778.83 3.39 26.47 0.00 33 2.75 22.73 1129.38 766.47 3.39 26.47 0.00 34 2.83 22.73 1124.51 754.80 3.39 26.47 0.00 35 2.92 22.73 1119.1,8 743.14 3.39 26.47 0.00 36 3.00 22.73 1113.60 730.78 3.39 26.47 0.00 37 3.08 22.73 1107.50 718.44 3.39 26.47 0.00 38 3.17 22.73 1101.20 706.93 3.39 26.47 0.00 39 3.25 22.73 1094.28 695.53 3.39 26.47 0.00 40 3.33 22.73 1087.15 683.49 3.39 26.47 0.00 41 3.42 22.73 1079.25 671.61 3.39 26.47 0.00 42 3.50 22.75 1071.16 660.71 3.39 26.47 0.00 43 3.58 22.73 1062.14 650.01' 3.39 26.47 0.00 44 3.67 22.73 1052.87 638.76 3.39 26.47 0.00 45 3.75 22.73 1042.42 627.81 3.39 26.47 0.00 46 3.83 22.73 1031.72 618.01 3.39 26.47 0.00 47 3.92 22.75 1019.52 608.51 3.39 26.47 0.00 48 4.00 22.73 1007.00 598.54 3.39 26.47 0.00 49 4.08 22.73 992.53 589.02 3.39 26.47 0.00 50 4.17 22.73 's 977.73 580.84 3.39 26.47 0.00 51 4.25 22.73 960.48 573.04 3.39 26.47 0.00 52 4.33 22.73 942.79 564.83 3.39 26.47 0.00 53 4.42 22.73 921.99 557.22 3.39 26.47 0.00 54 4.50 22.73 900.71 551.14 3.39 26.47 0.00 55 4.58 22.73 875.59 545.47 3.39 2', 47 0.00 56 4.67 22.73 849.93 539.55 3.39 2:.47 0.00 57 4.75 22.73 819.51 534.24 3.39 26.47 0.00 58 4.83 22.73 788.53 530.36 3.39 26.47 0.00 59 4.92 22.73 787.90 527.05 3.39 26.47 0.00 6C 5.00 22.73 751.15 523.82 3.39 26.47 0.00 61 5.08 22.73 713.82 520.35 3.39 26.47 0.00 62 5.17 22.73 669.48 517.46 3.39 26.47 0.00 63 5.25 22.73 624.55 516.08 3.39 26.47 0.00 64 5.33 22.73 571.22 515.26 3.39 26.47 0.00 STEAM PRODUCED = 1.05 STEAM SURPLUS : 1.05 MOLES HODE CORE HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH
<1 0.08 27.13 1250.57 1264.11 2.82 26.46 0.01 2
0.17 27.13 1261. 7 1265.38 2.82 26.46 0.01 8
'3 0.25 27.13 1272.25 1265.19 2.82 26.46 0.01 4
0.33 27.13 1281.72 1264.52 2.82 26.46 0.01
,5 0.42 27.13 1290.31 1263.88 2.82 26.46 0.01 6:
0.50 27.13 1298.03 1262.37 2.82 26.46 0.01 7
0.58 27.13 1304.90 1259.46 2.82 PS.46 0.01
- < 8.
.0.67 27.13 1310.95 1256.03 2.82 26.45 0.01 9
0.75 27.13 1316.21 1252.63 2.82 26.45,'
0.02 26.45 O.02 10 0.83 27.13 1320.70 1248.47 2.82
~
11 0.92 i7,13 1324.43 1242.99 2.82 26.45 0.02 12 1.00 27.13 1327.43 1236.98 2.82 26.45 0.02 13 1.08 27.13 1329.73 1231.08 2.82 26.45 0.02 14 FA) 1.17 27.13 1331.35 1224.55 2.82 26.45 0.02 15 rNJ 1.25 27.13 1332.31 1216.65 2.82 26.45 0.02 16 ps) 1.33 27.13 1332.63 1208.29 2.82 26.45 0.02 17 45, 1.42 27.13 1332.36 1200.22 2.82 26.45 0.02 1.50 27.13 1331.51 1191.63 2.82 26.45 0.02 13 1 19 1.58 27.13 1330.09 1181. 2 2.82 26.45 0.02 8
20 INJ 1.67 27.13 1328.16 1171.68 2.82 26.45 0.02 21 wi) -
1.75 27.13 1325.69 1160.487 2.82 26.45 0.02 22 amJ 1.83 27.13 1322.74 1150.28 2.82 26.45 0.02
23 1.92 27.13 1319.33 1139.30 2.82 26.45 0.01 24 2.00 27.13 1315.47 1127.32 2.82 26.45 0.01 25 2.08 27.13 1311.18 1114.91 2.82 26.45 0.01 26 2.17 27.13 1306.52 1102.77 2.82 26.45 3.01 27 2.25 27.13 1301.4'7 1090.38 2.82 26.45 0.01 28 2.33 27.13 1296.07 1077.05 2.82 26.45 0.01 29 2.42 27.13 1290.33 1063.37 2.82 26.45 0.01 30 2.50 27.13 1284.30 1050.05 2.82 26.45 0.01 31 2.58 27.13 1277.97 1036.57 2.82 26.45 0.01 32 2.67 27.13 1271.36 1022.25 2.82 26.46 0.01 33 2.75 27.13 1264.49 1007.63 2.82 26.46 0.01 34 2.83 27.13 1257.41 993.47 2.82 26.46 0.01 35 2.92 27.13 1250.10 979.24 2.82 26.46 0.01 36 3.00 27.13 1242.59 964.24 2.82 26.46 0.01 37 3.08 27.13 1234.87 949.02 2.82 26.46 0.01 38 3.17 27.13 1227.03 934.35 2.82 26.46 0.01 39 3.25 27.13 1218.99 919.70 2.82 26.46 0.01 40 3.33 27.13 1210. 4 904.33 2.82 26.46 0.01 8
41 3.42 27.13 1202.50 888.81 2.82 26.47 0.01 42 3.50 27.13 1194.11 873.95 2.82 26.47 0.00 43 3.58 27.13 ',
1185.54 859.18 2.82 26.47 0.00 44 3.67 27.13 1176.90 843.74 2.82 26.47 0.00 45 3.75 27.13 1168.08 828.23 2.82 26.47 0.00 46 3.83 27.13 1159.25 813.49 2.82 26.47 0.00 47 3.92 27.13 1150.19 798.90 2.82 26.47 0.00 48 4.00 27.13 1141.13 783.69 2.82 26.47 0.00 49 4.08 27.13 1131.75 768.50 2.82 26.47 0.00 50 4.17 27.13 1122.42 754.18 2.82 26.47 0.00 51 4.25 27.13 1112.72 740.10 2.82 26.47 0.00 52 4.33 27.13 1103.03 725.43 2.82 26.47 0.00 53 4.42 27.13 1092.80 710.88 2.82 26.47 0.00 54 4.50 27.13 1082.61 697.34 2.82 26.47 0.00 55 4.58 27.13 1071.73 684.09 2.82 26.47 0.00 55 4.67 27.13 1060.82 670.47 2.82 26.47 0.00 57 4.75 27.13 1048.97 657.02 2.82 26.47 0.00 58 4.83 27.13 1037.07 644.55 2.82 26.47 0.00 59 4.92 27.13 1032.50 632.57 2.82 26.47 0.00 60 5.00 27.13 1019.47 620.87 2.82 26.47 0.00 ps) i 61 5.08 27.13 1006.31 608.98 2.82 26.47 0.00 62 IN) 5.17 27.13 991.43 597.42 2.82 26.47 0.00 63 IN) 5.25 27.13 976.40 587.07 2.82 26.47 0.00 64 Jd.
5.33 27.13 959.08 577.42 2.82 26.47 0.00 65 5.42 27.13 941.46 567.67 2.82 26.47 0.00 5.50 27.13 920.84 558.39 2.82 26.47 0.00 66 pg) 67 5.58 27.13 899.85 550.53 2.82 26.47 0.00
'I) 5.67 27.13 875.01 543.49 2.82 26.47 0.00 68 i
69 LJ1 5.75 27.13 849.61 536.39 2.82 26.47
0.00 70 5.83 27.13 819.35 529.85 2.82 26.47 O.00 71 5.92 27.13 788.45 524.89 2.82 26.47 0.00 72 6.00 27.13 751.52 520.80 2.82 26.47 0.00 73 6.08 27.13 713.30 516.61 2.82 26.47 0.00 74 6.17 27.13 668.71 513.00 2.82 26.47 0.00 75 6.25 27.13 622.75 511.07 2.82 26.47 0.00 76 6.33 27.13 567.88 510.03 2.82 26.47 0.00 STEAM PRODUCED = 0.87 STEAM SURPLUS : 0.87 MOLES
.HODE.
CORE HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH
~
1 0.08 31.53 1528.07 1557.71 2.23 26.39 0.06 2
0.17 31.53 1539.37 1561. 8 2.23 26.38 0.06 8
<3 0.25 31.53 1549.57 1564.39 2,23 26.38 0.06
4 0.33 31.53 1556.19 1566.18 2.23 26.37 0.07 5
0.42 31.53 1563.99 1568.09 2.23 26.37 0.07 6
0.50 31.53 1570.82 1569.00 2.23 26.36 0.07 7
0.58 31.53 1576.69 1568.39 2.23 26.36 0.07 8
0.67 31.53 1581.63 1567.09 2.23 26.35 0.07 9
0.75 31.53 1585.66 1565.66 2.23 26.35 0.07 to 0.83 31.53 1588.81 1563.35 2.23 26.35 0.07 11 0.92 31.53 1591.09 1559.63 2.23 26.35 0.08 12 1.00 31.53 1592.54 1555.20 2.23 26.34 0.08 13 1.08 31.53 1593.19 1550.71 2.23 26.34 0.08 14 1.17 31.53 1593.05 1545.50 2.23
?6.34 0.08 15 1.25 31.53 1592.16 1538.83 2.23 i6.54 0.07 16 1.33 31.53 1590.54 1531. 3 2.23 26.34 0.07 5
17 1.42 31.53 1588.23 1524.35 2.23 26.34 0.07 18 1.50 31.53 1585.25 1516.58 2.25 26.35 0.07 19 1.58 31.53 1581.62 1507.53 2.23 26.35 0.07 20 1.67 31.53 1577.38 1498.00 2.23 26.35 0.07 21 1.75 31.53 1572.55 1487.67 2.23 26.35 0.07 22 1.83 31.53 1567.17 1477.39 2.23 26.36 0.07 23 1.92 31.53 1561.25 1466.65 2.25 26.36 0.06 24 2.00 31.53
's 1334.83 1454.84 2.23 26.36 0.06 25 2.08 31.53 1547.93 1442.46 2.23 26.37 0.06 26 2.17 31.53 1542.47 1430.17 2.23 26.37 0.06 27 2.25 31.53 1534.38 1417.34 2.23 26.37 0.06 28!
2.33 31.53 1525.86 1403.55 2.23 26.38 0.05 29 2.42 31.53 1516.96 1389.26 2.23 26.38 0.05 30 2.50 31.53 1507.71 1375.17 2.23 26.39 0.05 31 2.58 31.53 1498.14 1360.86 2.23 26.39 0.05 32 2.67 31.53 1488.25 1345.68 2.23 26.40 0.04 33 2.75 31.53 1478.09 1330.08 2.23 26.40 0.04 34 2.83 31.53 1467.67 1314.75 2.23 26.40 0.04 35 2.92 31.53 1457.02 1299.30 2.25 26.41 0.04 36 3.00 31.53 1446.16 1283.06 2.23 26.41 0.03 37 3.08 31.53 1435.10 1266.45 2.23 26.42 0.03 38 3.17 31.53 1423.89 1250.21 2.23 26.42 0.03 39 3.25 31.53 1412.53 1233.92 2.23 26.43 0.03 40 3.33 31.53 1401.05 1216. 9 2.23 26.43 0.03 8
41 3.42 31.53 1389.45 1199.56 2.23 26.43 0.02 42 3.50 31.53 1377.79 1182.65 2.23 26.44 0.02 43 3.58 31.53
.26.05 1165.78 2.23 26.44 0.02 44 3.67 31.53 1354.27 1148.20 2.25 26.44 0.02 45 3.75 31.53 1342.44 1130.36 2.23 26.44 0.02
~
46 3.83 31.53 1330.62 1113.02 2.23 26.45 0.02 47 3.92 31.53 131-8.79 1095.75 2.23 26.45 0.02 48 4.00 31.53 1306.99 1077.80 2.23 26.45 0.01 47 4.08 31.53 1295.18 1059.62 2.23 26.45 0.01 50 4.17 31.53 1283.45 1042.00 2.23 26.46 0.01 51 4.25 31.53 1271.76 1024.49 2.23 26.46 %
a 01 52 4.33 31.53 1260.15 1006.28 2.23 26.46 0.01 53 PA) 4.42 31.53 1248.56 987.87 2.23 26.46 0.01 54 rs) 4.50 31.53 1237.11 970.06 2.23 26.46 0.01 55 rs) 4.58 31.53 1225.70 952.35 2.23 26.46 0.01 56 4.67 31.53 1214.40 934.06 2.23 26.47 0.01 43, 57 4.75 31.53 1203.13 915.54 2.23 26.47 0.01 58 4.83 31.53 1192.00 897.47 2.23 26.47 0.00 59 FN3 4.92 31.53 1182.36 879.54 2.23 26.47 0.00
. 60 si) 5.00 31.53 1171.39 861.76 2.23 26.47 0.00 67 cys 5.08 31.53 1160.57 843.53 2.23 26.47 0.00 62 3.17 31.53 1149.67 825.12 2.25 26.47 0.00 63 5.25 31.53 1138.98 807.31 2.23 26.47 0.b0 O
64 5.33 31.53 1128.08 789.83 2.25 26.47 0.00 65 5.42 31.53 1117.35 771.95 2.25 26.47 0.00 66 5.50 31.53 1106.26 753.97 2.23 26.47 0.00 67 5.58 31.53 1095.35 736.74 2.23 26.47 0.00 68 5.67 31.53 1083.90 719.97 2.23 26.47 0.00 69 5.75 31.53 1072.52 702.91 2.23 26.47 0.00 70 5.83 31.53 1060.29 685.88 2.23 26.47 0.00 71 5.92 31.53 1048.15 669.81 2.23 26.47 0.00 72 6.00 31.53 1034.79 654.42 2.25 26.47 0.00
(
73 6.08 31.53 1021.38 638.91 2.25 26.47 0.00 74 6.17 31.53 1006.23 623.63 2.23 26.47 0.00 75 6.25 31.53 990.97 609.60 2.23 26.47 0.00 76 6.33 31.53 973.37 596.53 2.23 26.47 0.00 77 6.42 31.53 955.44 583.54 2.23 26.47 0.00 78 6.50 31.53 934.39 571.00 2.23 26.47 0.00 79 6.58 31.53 912.89 560.05 2.23 26.47 0.00 80 6.67 31.53 887.34 550.33 2.23 26.47 0.00 81 6.75 31.53 861.09 540.84 2.23 26.47 0.00 82 6.83 31.53 829.68 531.94 2.23 26.47 0.00 83 6.92 31.53 797.47 524.91 2.23 26.47 0.00 84 7.00 31.53 ',
758.83 519.26 2.23 26.47 0.00 85 7.08 31.53 719.24 513.81 2.23 26.47 0.00 4
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'87 7.25 31.53 623.37 506.06 2.23 26.47 0.00 88 7.33 31.53 565.52 504.64 2.23 26.47 0.00 STEAM PRODUCED : 0.69 STEAM SURPLUS : 0.68 MOLES HODE CORE HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH o1 0.08 35.93 1564.74 1903.73 1.72 26.08 0.21
'2 0.17 35.93 1879.73 1913.39 1.72 26.06 0.23 3
0.25 35.93 1893.37 1921.12 1.72 26.04 0.24
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0.42 35.93 1916.74 1934.01 1.72 26.01 0.26
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0.58 35.93 1934.59 1941.53 1.72 25.98 0.27
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0.75 35.93 1946.30 1944.27 1.72 25.96 0.28 to 0.83 35.93 1950.26 1944.20 1.72 25.95 0.29
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1504.04 1360.47 1.72 26.40 0.05 54 4.50 35.93 1488.60 1341.14 1.72 26.40 0.05 55 4.58 35.93 1473.25 1321. 7 1.72 26.41 0.04 8
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61 5.08 35.93 1383.38 1201.41 1.72 26.44 0.03 62 5.17 35.93 1368.79 1180.53 1.72 26.44 0.02 63 5.25 35.93 1354.37 1159.90 1.72 26.45 0.02 64 5.33 35.93 1340.07 1139.36 1.72 26.45 0.02 65 5.42 35.93 1325.94 1118.23 1.72 26.45 0.02 66 5.50 35.93 1311.91 1096.64 1.72 26.45 0.02 67 5.58 35.93 1298.08 1075.28 1.72 26.46 0.01 68 5.67 35.93 1284.37 1054.02 1.72 26.46 0.01 69 5.75 35.93 1270.82 1032.14 1.72 26.46 0.01 70 5.83 35.93 1257.33 1009.77 1.72 26.46 0.01 71 5.92 35.93 1244.07 987.66 1.7" 26.46 0.01 72 6.00 35.93 1230.84 965.68 1,72 26.47 0.01 73 6.08 35.93 1217.79 943.11 1.7-2 26.47 0.01 74 6.17 35.93 1204.67 920.05 1.72 26.47 0.01 75 6.25 35.93 1191.78 897.33 1.72 26.47 0.00 76 6.33 35.93 1178.72 874.86 1.72 26.47 0.00 77 6.42 35.93 1165.83 851.88 1.72 26.47 0.00 78 6.50 35.93 1152.60 828.50 1.72 26.47 0.00 79 6.58 35.93 1139.55 805.64 1.72 26.47 0.00 80 6.67 35.93 1125.97 783.26 1.72 26.47
O.00 81 6.75 35.93 1112.46 760.57 1.72 26.47 0.00 32 6.83 35.93 1098.09 737.66 1.72 26.47 0.00 83 6.92 35.93 1083.79 715.59 1.72 26.47 0.00 84 7.00 35.93 1068.25 694.37 1,72 26.47 0.00 85 rs) 7.08 35.93 1052.65 673.18 1.72 26.47 0.00 l
36 rs) 7.17 35.93 1035.25 652.07 1.72 26.47 0.00 87 7.25 35.93 1017.'2 632.28 1.72 26.47 0.00 7
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93 7.75 35.93 872.75 536.00 1.72 26.47 0.00 94 7.83 35.93 838.59 523.67 1.72 26.47 0.00 95 7.92 35.93 803.67 513.61 1.72 26.47 0.00 96 8.00 35.93 762.28 505.77 1.72 26.47 0.00 STEAM PRODUCED = 0.53 STEAM SURPLUS : 0.52 MOLES HODE' CORE HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH 1
0.08 38.87 2235.93 2268.27 1.72 25.37 0.67 2
0.17 38.87 2252.94 2280.04 1.72 25.32 0.69 3
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0.42 38.87 2292.07 2303.65 1.72 25.19 0.76 6
0.50 38.87 2301.17 2308.39 1.72 25.15 0.77 7
0.58 38.87 2308.36 2310.77 1.72 25.13 0.78 8
0.67 38.87 2313.72 2311.60 1.72 25.10 0.79 9
0.75 38.87 2317.33 2311.48 1.72 25.08 0.79 10 0.83 38.87 2319.25 2309.77 1.72 25.07 0.80 11 0.92 38.87 2319.55 2305.98 1.72 0%.07 0.80 12 1.00 38.87 2518.30 2300.79 1.72 25.w' O.79 13 1.08 38.87 2315.57 2294.87 1.72 25.07 0.78 14 1.17 38.87 's 2311.43 2287.71 1.72 25.08 0.77 15 1.25 38.87 2305.96 2278.63 1.72 25.09 0.76 16 1.33 38.87 2299.23 2268.38 1.72 25.11 0.75 17 1.42 38.87 2291.33 2257.76 1.72 25.13 0.73 18 1.50 38.87 2282.32 2246.22 1.72 25.15 0.72 19 1.58 38.87 2272.27 2233.16 1.72 25.18 0.70 20 1.67 38.87 2261.27 2219.30 1.72 25.21 0.68 21 1.75 38.87 2249.37 2204.38 1.72 25.24 0.66 22 1.83 38.87 2236.67 2189.24 1,72 25.28 0.64 23 1.92 38.87 2223.24 2173.52 1.72 25.31 0.61 24 2.00 38.87 2209.12 2156.69 1.72 25.35 0.59 25 2.08 38.87 2194.36 2139.14 1.72 25.39 0.57 26 2.17 38.87 2178.99 2121.52 1.72 25.43 0.55 27 2.25 38.87 2163.13 2103.61 1.72 25.47 0.52 28 2.33 38.87 2146.77 2084.79 1.72 25.51 0.50 29 2.42 38.87 2129.92 2065.41 1.72 25.55 0.48 30 2.50 38.87 2112.76 2046.14 1.72 25.59 0.45 31
?.58 38.87 2095.29 2026.70 1.72 25.63 0.43 32 2.67 38.87 2077.53 2006.47 1.72 25.67 0.41 33 2.75 38.87 2059.51 1985.78 1.72 25.71 0.39 34i 2.83 38.87 2041.06 1965.30 1.72 25.75 0.37 35 2.92 38.87 2022.55 1944.86 1.72 25.79 0.35
.36 3.00 38.87 2003.95 1923.87 1.72 25.83 0.33 37 3.08 38.87 1985.24 1902.54 1.72 25.86 0.31 38 3.17 38.87 1966.14 1881.51 1.72 25.90 0.29 39 3.25 38.87 1947.01 1860.60 1.72 25.93 0.28 40 3.33 38.87 1928.01 1839.11 1.72 25.96 0.26
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a 54 4.50 38.87 1666.16 1544.59 1.72 26.28 0.10 55 4.58 38.87 1649.24 1523.72 1.72 26.29 0.09 56 4.67 38.87 1632.32 1502.21 1.72 26.31 0.09 57 4.75 38.87 1616.08 1480.19 1.72 26.32 0.08 58 4.83 38.87 1598.88 1458.12 1.72 26.33 0.08 59 4.92 38.87 1582.99 1435.90 1.72 26.34 0.07 60 5.00 38.87 1565.48 1413.44 1.72 26.36 0.07 61 5.08 38.87 1548.05 1390.44 1.72 26.37 0.06 1
62 5.17 38.87 1532.24 1366.97 1.72 26.38 0.06 63 5.25 38.87 1514.46 1343.41 1.72 26.39 0.05 64 5.33 38.87 1496.83 1319.94 1.72 26.39 0.05 65 5.42 38.87 1479.32 1295.92 1.72 26.40 0.04 66 5.50 38.87 1461.96 1271.42 1.72 26.41 0.04 67 5.58 38.87 1444.77 1247.07' 1.72 26.42 0.04 68 5.67 38.87 1427.75 1222.79 1.72 26.42 0.03 69 5.75 38.87 1410. <8 6 1197.92 1,72 26.43 0.03 70 5.83 38.87 1394.14 1172.51 1.72 26.45 0.03 71 5.92 38.87 1377.62 1147.23 1.72 26.44 0.02 l
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80 6.67 38.87 1236.88 909.94 1.72 26.46 0.01 81 6.75 38.87 1222.10 882.74 1.72 26.46 0.01 82 6.83 38.87 1207.31 855.07 1.72 26.47 0.01 83 6.92 38.87 1192.79 827.77 1.72 26.47 0.01 84 7.00 38.87 1178.14 800.98 1.72 26.47 0.00 85 7.08 38.87 1163.'1 773.96 1.72 26.47 0.00 7
86 7.17 38.87 1148.96 746.64 1.72 26.47 0.00 87 7.25 38.87 1134.44 719.99 1.72 26.47 0.00 88 7.33 38.87 1119.3-8 694.25 1.72 26.47 0.00 89 7.42 38.87 1104.48 668.65 1.72 26.47 0.00 90 7.50 38.87 1088.72 643.08 1.72 26.47 0.00 91 7.58 38.87 1073.10 618.66 1.72 26.87 0.00 92 7.67 38.87 1056.17 595.74 1.72 26.47 0.00 93 7.75 38.87 1039.27 573.52 1.72 26.47 0.00 94 7.83 38.87 1020.59 551.79 1.72 26.47 0.00 95 7.92 38.87 1001.77 531.83 1.72 26.47 0.00 96 8.00 38.87 980.55 514.07 1.72 26.47 0.00 STEAM PRODUCED 0.53 STEAM SURPLUS : 0.50 MOLES NODE CORE HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH 1
0.08 43.27 3504.61 3506.60 1.73 18.72,'
6.32 2
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0.50 43.27 3490.78 3468.66 1.73 18.41 6.00 0.58 43.27 3473.88 3447.45 1.73 18.47 5.84
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- 48 4.00 43.27 2078.50 1971.86 1.73 25.54 0.37 49 4.08 43.27 2050.56 1940.85 1.70 25.61 0.34 50 4.17 43.27 2022.95 1910.46 1.73 25.67 0.31 51 4.25 43.27 1995.63 1880.54 1.73 25.73 0.29 52 4.33 43.27 1968.70 1850.36 1.73 25.79 0.26 53 4.42 43.27 1941.97 1820.05 1.73 25.84 0.24 54 4.50 43.27 1915.60 1790.28 1.73 25.89 0.22 55 4.58 43.27 1889.36 1760.84 1.73 25.94 0.20 56 4.67 43.27 1863.53 1731.19 1.73 25.98 0.18 57 4.75 43.27 1837.57 1701.34 1.75 26.02 0.17 58 4.83 43.27 1811. 0 1671.90 1.73 26.06 0.15 8
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75 6.25 43.27 1432.71 1162.57 1.73 26.40 0.03 76 6.33 43.27 1412.26 1130.99 1.73 26.41 0.02 77 6.42 43.27 1392.12 1099.04 1.73 26.41 0.02 78 6.50 43.27 1372.33 1066.62 1.73 26.42 0.02 79 6.58 43.27 1352.92 1034.32 1.73 26.43 0.02 80 6.67 43.27 1333.89 1002.33 1.73 26.43 0.02 81 6.75 43.27 1315.21 970.06 1.73 26.44 0.01 82 6.83 43.27 1296.90 937.38 1.73 26.44 0.01 83 6.92 43.27 1279.00 904.94 1.73 26.45 0.01 84 7.00 43.27 1261.48 872.97 1.73 26.45 0.01 85 7.08 43.27 1244.37 840.93 1.73 26.45 0.01 86 7.17 43.27 1227.6L 808.62 1.73 26.46 0.01 87 7.25 43.27 1211.28 776.74 8.73 26.46 0.01 88 7.33 43.27 1195.29 745.66 1.73 26.46 0.00 89 7.42 43.27 1179.75 714.87 1.73 26.46 0.00 90 7.50 43.27 1164.49 684.15 1.73 26.47 0.00 91 7.58 43.27 1149.74 654.22 1.73 26.47 0.00 92 7.67 43.27 1135.19 625.61 1.75 26.47 0.00 93 7.75 43.27 1121.16 597.95 1.73 26.47 0.00 94 7.83 43.27 1107.35 571.00 1.73 26.47 0.00 95 7.92 43.27 8,
1094.04 545.44 1.75 26.47 0.00 96 8.00 43.27 1080.91 521.86 1.73 26.47 0.00 STEAM PRODUCED : 0.53 STEAM SURPLUS : 0.36 MOLES HODE CORE HEIGHT-FT TIME-MIH FUEL DEG-F
EAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH 1
0.08 47.67 3766.64 3769.38 1.74 17.81 6.32 t2 0.17 47.67 3771.90 3773.27 1.74 17.74 6.33 i3 0.25 47.67 3776.05 3775.46 1.74 17.65 6.31 4
0.33 47.67 3779.05 3776.87 1.74 17.59 6.24
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0.08 56.47 4158.24 4158.79 1.80
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0.08 60.87 4280.09 4276.76 1.84 17.81 6.32 2
0.17 60.87 4276.20 4271.19 1.84 17.74 6.33
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2.58 60.87 3288.05 3227.80 1.84 14.05 5.18 32 N
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3.17 60.87 2911.19 2799.76 1.84 7.97 0.67
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1925.10 1754.88 1.84 24.73 0.09 60 5.00 60.87 1892.25 1716.90 1.84 24.91 0.08 61 5.08 60.87 V860.12 1679.33 1.84 25.07 0.07 62 5.17 60.87 1828.70 1641.99 1.84 25.21 0.06 63 5.25 60.87 1797.98 1605.08 1.84 25.34 0.06 64 5.33 60.87 1768.05 1568.74 1.84 25.46 0.05 65 5.42 60.87 1738.91 1532.64 1.84 25.57 0.05 66 5.50 60.87 1710.33 1496.58 1.84 25.66 0.04
'67 5.58 60.87 1682.31 1460.79 1.84 25.75 0.04 65 5.67 60.87 1654.86 1425.41 1.84 25.82 0.03 69 5.75 60.87 1627.71 1390.20 1.84 25.89 1.03 70 5.83 60.87 1601.05 1355.05 1.84 25.95 0.03 71 5.92 60.87 1575.91 1320.12 1.84 26.01 0.02 72 6.00 60.87 1549.61 1285.62 1.84 26.06 0.02 73 6.08 60.87 15.M. 81 1251.33 1.84 26.11 0.02 74 6.17 60.87 1500.61 1217.05 1.84 26.15 6.02 75 6.25 60.87 1476.88 1182.94 1.84 26.19 0.01 76 6.33 60.87 1454.00 1149.22 1.84 26.22 0.01 77 6.42 60.87 1431.67 1115.71 1.84 26.25 0.01 78 6.50 60.87 1409.91 1082.19 1.84 26.27 0.01 79 6.58 60.87 1388.72 1048.82 1.84 26.30 0.01 80 6.67 60.87 1368.11 1015.83 1.84 26.32 0.01 81 6.75 60.87 17'e 8. 0 3 983.11 1.84 26.34 0.01 82 6.83 60.87 1328.54 950.47 1.84 26.35 0.01 83 6.92 60.87 1309.60 918.04 1.84 26.37 0.01 84 7.00 60.87 1291.23 886.07 1.84 26.38 0.01 85 7.08 60.87 1273.42 854.54 1.84 26.39 0.00 N
36 7.17 60.87 1256.17 823.29 1.34 26.40
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92 7.67 60.87 1164.94 648.72 1.84 26.44 0.00 93 O
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, STEAM PRODUCED.: 0.57 STEAM SURPLi'i 4 d.56 MOLES 4,
HODE CORE HEIGHT-FT TIME-MIH FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH 1
0.08 65.27 4272.20 4259.54 1.89 17.8 1 6.32 2
0.17 65.27 4252.65 4237.68 1.89 17.74 6.33 3
0.25 65.27 4230.30 4212.59 1.89 17.65 6.31 4
0.33 65.27 4205.16 4184.80 1.49 17.59 6.24 5
0.42 65.27 4177.25 4154.95 1.89 17.52 6.14 6
0.50 65.27 4146.65 4122.34 1.89 17.41 6.00 7
0.58 65.27 4113.43 4086.66 1.89 17.35 5.84 8
0.67 65.27 4077.71 4048.63 1.89 17.26 5.66 9
0.75 65.27 4039.65 4009.11 1.89 17.21 5.46 10 0.83 65.27 3999.42 3967.83 1.89 17.14 5.25 11 0.92 65.27 3957.24 3924.71 1.89 17.10 5.02 12 1.00 65.27 3913.35 3880.61 1.89 17.03 4.79 13 1.08 65.27 3868.00 3835.92 1.89 16.89 4.56 14 1.17 65.27 3821.43 3787.76 1.89 16.74 6.18 15 1.25 65.27 3773.90 3737.35 1.89 16.63 5.77 16 1.33 65.27 3725.67 3685.65 1.89 16.62 5.38 17 1.42 65.27 3676.98 3633.21 1.89 16.52 5.01 18 1.50 65.27 3628.03 3580.23 1.89 16.40 4.65 19 1.58 65.27 3579.03 3529.56 1.89 16.28 5.93 20 1.67 65.27 ',
3530.18 3480.98 1.89 16.21 5.43 4
21 1.75 65.27 3481.60 3433.44 1.89 16.11 4.96 22 1.83 65.27 3433.43 3386.58 1.89 15.88 6.09 23 1.92 65.27 3385.66 3335.74 1.89 15.84 5.49 24 2.00 65.27 3338.36 3284.21 1.89 15.72 4.95 25 2.08 65.27 3291.57 3233.87 1.89 15.49 5.83 26 2.17 65.27 3245.39 3188.79 1.89 15.39 5.19 27 2.25 65.27 3199.81 3144.75 1.89 15.17 4.63 28 2.33 65.27 3154.72 3095.84 1.89 14.94 5.19 29 2.42 65.27 3110.12 3046.52 1.89 14.67 4.58 30 2.50 65.27 3066.14 3003.63 1.89 14.41 4.95 l
31 2.58 65.27 3022.67 2959.37 1.89 14.05 5.18 e
32 2.67 65.27 2979.64 2912.66 1.89 13.59 5.24 l
33 2.75 65.27 2937.18 2871.29 1.89 12.97 4.47 i
- 34..
2.83 65.27 2895.10 2824.78 1.89 12.03 4.75 35 2.92 65.27 2853.52 2781.75 1.89 10.27 4.40 1
36 3.00 65.27 2831.55 2737.85 1.89 0.12 0.34 37 3.08 65.27 2779.88 2683.22 1.89 3.82 0.34 38 3.17 65.27 2729.11 2629.64 1.89 6.83 0.33 i
39 3.25 65.27 2679.35 2577.30 1.89 9.31 0.32 l
40 3.33 65.27 2630.67 2526.00 1.89 11.39 0.31 41 3.42 65.27 2583.08 2475.65 1.89 13.15 0.29 42 3.50 65.27 2536.61 2426.46 1.89 14.65 0.28 43 3.58 65.27 2491.26 2378.49 1.89 15.95 0.26 r
44 3.67 65.27 2447.01 2331.50 1.89 17.08 0.24 I
45 3.75 65.27 2403.83 2285.35 1.89 18.07 0.22 46 3.83 65.27 2361.69 2240.22 1.89 18.95 0.21 47 3.92 65.27 2320.57 2196.18 1.89 19.72 '
O.19 48 4.00 65.27 2280.42 2152.91 1.89 20.40 0.18 49 4.08 65.27 2241.21 2110.26 1.89 21.01 0.16 53 4.17 65.27 2202.89 2068.43 1.89 21.56 0.15 51 N
4.25 65.27 2165.44 2027.52 1.89 22.05 0.14 52 N
4.33 65.27 2128.83 1987.20 1.89 22.49 0.13 53 4.42 65.27 2093.00 1947.31 1.89 22.88 0.11 g
54 4.50 65.27 2057.96 1908.09 1.89 23.24 0.10 55 A
4.55 65.27 2023.66 1869.57 1.89 23.56 0.09 2 55 4.67 65.27 1990.06 1831.56 1.89 23.85 0.09 57 L r4 4.75 65.27 1957.17 1793.87 1.89 24.11 0.08 53 c>
4.83 65.27 1924.94 1756.64 1.89 24.35 0.07 65.27 1893.36 1719.82 1.89 24.56 0.06 4.92 59 e
60 5.00 65.27 1862.43 1683.52 1.89 24.75 0.06 61 5.08 65.27 1832.10 1647.58 1.89 24.95 C.05 62 5.17 65.27 1802.38 1611.79 1.89 25.09 0.05 63 5.25 65.27 1773.32 1576.33 1.89 25.23 0.04 64 5.33 65.27 1745.07 1541.32 1.89 25.36 0.04 65 5.42 65.27 1717.34 1506.50 1.89 25.47 0.04 66 5.50 65.27 1690.10 1471.71 1.89 25.58 0.03 67 5.58 65.27 1663.36 1437.11 1.89 25.67 0.03 68 5.67 65.27 1637.02 1402.85 1.89 25.76 0.03 1.
9 25.83 0.02 8
69 5.75 65.27 1680.90 1368.79 70 5.83 65.27 1585.36 1334.81 1.89 25.90 0.02 71 5.92 65.27 1560.42 1301.03 1.89 25.96 0.02 72 6.00 65.27 1536.08 1267.61 1.89 26.02 0.02 73 6.08 65.27 1512.30 1234.41 1.89 26.07 0.01 4
74 6.17 65.27 1488.89 1201.26 1.89 26.11 0.01 75 6.25 65.27 1466.38 1168.25 1.89 26.16 0.01 76 6.33 65.27 1444.44 1135.61 1.89 26.19 0.01 77 6.42 65.27 1423.01 1103.17 1.89 26.22 0.01 78 6.50 65.27 1402.14 1070.77 1.89 26.25 0.01 79 6.58 65.27 1381.80 1038.51 1.89 26.28 0.01 80 6.67 65.27 *,
1362.03 1006.57 1.89 26.30 0.01 1.
9 26.32 0.01 8
81 6.75 65.27 1342.76 974.93 1.
9 26.34 0.01 8
82 6.83 65.27 1324.05 943.44 83 6.92 65.27 1305.87 912.14 1.89 26.36 0.01 84 7.00 65.27 1288.24 881.25 1.89 26.37 0.00 85 7.08 65.27 1271.15 853.81 1.89 26.38 0.00 86 7.17 65.27 1254.60 820.71 1.89 26.39 0.00 87 7.25 65.27 1238.61 790.99 1.89 26.40 0.00 88 7.33 65.27 1223.15 761.85 1.89 26.41 0.00 89 7.42 65.27 1208.27 733.44 1.89 26.42 0.00 90 7.50 65.27 1193.97 705.76 1.89 26.43 0.00 91 7.58 65.27 1180.3C 678.89 1.89 26.43 0.00 92 7.67 65.27 1167.20 652.99 1.89 26.44 0.00 93 7.75 65.27 1154. 1 628.28 1.89 26.44 0.00 8
94 7.83 65.27 1143.16 604.97 1.89 26.45 0.00 95 7.92 65.27 1132.31 583.30 1.89 26.45 0.00 96 8.00 65.27 1122.39 563.61 1.89 26.45 0.00 STEAM PRODUCED = 0.58 STEAM SURPLUS : 0.58 MOLES HODE CORE HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH 1
0.08 69.67 4025.96 3999.05 1.94 17.81 6.32 2
0.17 69.67 3988.59 3959.79 1.94 17.74 6.33 3
0.25 69.67 3950.00 3919.06 1.94 17.65 6.31 4
0.33 69.67 3910.47 3877.64 1.94 17.59 6.24 5
0. c '_
69.67 3870.26 3836.33 1.94 17.52 6.14 6
0.50 69.67 3829.60 3794.65 1.94 17.41 6.00 7
0.58 69.67 3788.70 3752.38 1.94 17.35 5.84 8
0.67 69.67 3747.73 3710.21 1.94 17.26 %
5.66
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to 0.83 69.67 3666.06 3628.07 1.94 17.14 5.25 11 0.92 69.67 3625.54 3587.53 1.94 17.10 5.02 12 IN) 1 00 69.67 3535.30 3547.86 1.94 17.03 4.79 13 rs) 1.08 69.67 3545.37 3509.33 1.94 16.89 4.55 14 ps) 1.17 69.67 3505.73 3469.02 1.94 16.74 6.18 15 1.25 69.67 3466.36 3427.77 1.94 16.63 5.77 43, 1.33 69.67 3427.25 3386.14 1.94 16.62 5.38 16
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1.42 69.67 3388.36 3344.31 1.94 16.52 5.01
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13 L/4 1.50 69.67 3340.66 3302.12
't.94 16.40 4.65 1.58 69.67 3311.13 3261.95 1.94 16.25 5.93 19 69.67 3272.77 3223.53 1.94 16.21 5.43 2D
,'CCD 1.67
e 21 1.75 69.67 3234.55 3185.91 1.94 16.11 4.96 22 1.83 69.67 3196.48 3148.85 1.94 15.88 6.09 23 1.92 69.67 3158.46 3107.97 1.94 15.84 5.49 24 2.00 69.67 3120.48 3065.91 1.9v 15.72 4.95 25 2.08 69.67 3082.56 3024.19 1.94 15.49 5.83 26 2.17 69.67 3044.77 2986.69 1.94 15.39 5.19 27 2.25 69.67 3007.10 2950.00 1.94 15.17 4.63 28 2.33 69.67 2969.44 2908.62 1.94 14.94 5.19 29 2.42 69.67 2131.83 2866.18 1.94 14.67 4.58 30 2.50 69.67 2894.42 2829.08 1.94 14.41 4.95 31 2.58 69.67 2857.13 2790.62 1.94 14.05 5.18 32 2.67 67.67 2319.95 2749.62 1.94 13.59 5.24 33 2.75 69.67 2'/83.03 2713.27 1.94 12.97 4.47 34 2.83 69.67 2746.23 2672.18 1.94 12.03 4.75 35 2.92 69.67 2709.71 2633.96 1.94 10.27 4.40 36 3.00 69.67 2673.41 2594.85 1.94 0.0 0.0 37 3.08 69.67 2650.43 2556.46 1.94 3.17 0.20 38
' 3.1'7 69.67 2608.90 2511.65 1.94 6.19 0.20 39 3.25 69.67 2567.65 2467.31 1.94 8.69 0.20 40 3.33 69.67 2526.77 2423.33 1.94 10.80 0.19 41 3.42 69.67 's 2486.34 2379.67 1.94 12.58 0.19 42 3.50 69.67 2446.43 2336.57 1.94 14.12 0.18 43 3.58 69.67 2407.08 2294.12 1.94 15.45 0.17 44 3.67 69.67 2368.31 2252.17 1.94 16.62 0.16 45 3.75 69.67 2330.16 2210.64 1.94 17.64 0.15 3.83 69.67 2292.63 2169.71 1.94 18.54 0.14 46 47 3.92 69.67 2255.74 2129.48 1.94 19.34 0.13 48 4.00 69.67 2219.49 2089.74 1.94 20.06 0.12 49 4.08 69.67 2183.85 2050.35 1.94 20.70 0.11 50 4.17 69.67 2148.85 2011.50 1.94 21.27 0.11 51 4.25 69.67 2114.47 1973.32 1.94 21.78 0.10 52 4.33 69.67 2080.71 1935.56 1.94 22.24 0.09 53 4.42 69.67 2047.54 1598.07 1.94 22.66 0.08 54 4.50 69.67 2014.96 1861.05 1.94 23.03 0.08 55 4.58 69.67 1982.98 1824.58 1.94 23.37 0.07 56 4.67 69.67 1951.56 1788.51 1.94 23.68 0.06 57 4.75 69.67 1920.71 1752.68 1.94 23.96 0.06 58 4.83 69.67 1890.42 1717.20 1.94 24.21 0.05 59 4.92 69.67 1860.67 1682.03 1.94 24.43 0.05 60 5.00 69.67 1831.48 1647.29 1.94 24.64 0.04 61 5.08 69.67 1802.81 1612. 6 1.94 24.82 0.04 8
62 5.17 69.67 1774.73 1578.56 1.94 24.99 0.04 63 5.25 69.67 1747.43 1544.50 1.94 25.14 0.03 64 5.33 69.67 1720.62 1510.76 1.94 25.28 0.03 65 5.42 69.67 1694.26 1477.21 1.94 25.40 0.03 66 5.50 69.67 1668.34 1443.70 1.94 25.51 0.02 67 5.58 69.67 1642.83 1410.32 1.94 25.61.'
0.02 68 5.67 69.67 1617.45 1377.24 1.94 25.70 O.02
." 69 5.75 69.67 1592.53 1344.41 1.94 25.79 0.02 70 5.83 69.67 1568.18 1311.68 1.94 25.86 0.02 I\\)
71 5.92 69.67 1544.39 1279.11 1.94 25.93 0.01 72 PN) 6.00 69.67 1521.16 1246.87 1.94 25.98 0.01 73 PNJ 6.08 69.67 1498.36 1214.86 1.94 26.04 0.01 74 42.
6.17 69.67 1476.15 1882.94 1.94 26.09 0.01 75 6.25 69.67 1454.68 1151.16 1.94 26.13 0.01 6.33 69.67 1433.74 1119.65 1.94 26.17 0.01 76 6.42 69.67 14i3.30 1088.39 1.94 26.20 0.01
. 77 78-6.50 69.67 1393.38 1057.21 1.94 26.23 0.01 6.58 69.67 1373.97 1026.17 1.94 26.26 0.01 7?
80 6.67 69.67 1355.10 995.42 1.94 26.29 0.01
a 81 6.75 69.67 1336.71 964.99 1.94 26.31 0.01 82 6.83 69.67 1318.85 934.76 1.94 26.33 0.01 83 6.92 69.67 1301.51 904.74 1.94 26.35 0.00 84 7.00 69.67 1284.69 875.11 1.94 26.36 0.00 85 7.08 69.67 1268.39 845.93 1.94 26.37 0.00 86
- 7. ~ 7 69.67 1252.61 817.15 1.94 26.39 0.00 87 7.25 69.67 1237.37 788.78 1.94 26.40 0.00 88 7.33 69.67 1222.65 760.97 1.94 26.41 0.00 39 7.42 69.67 1208.49 733.86 1.94 26.41 0.00 90 7.50 69.67 1194.89 707.53 1.94 26.42 0.00 91 7.58 69.67 1181.91 682.03 1.94 26.43 0.00 92 7.67 69.67 1169.49 657.51 1.94 26.43 0.00 93 7.75 69.67 1157.76 634.19 1.94 26.44 0.00 94 7.83 69.67 1146.77 612.24' 1.94 26.44 0.00 95 7.92 69.67 1136.56 591.91 1.94 26.45 0.00 96 8.00 69.67 1127.27 573.55 1.94 26.45 0.00 STEAM PRODUCED : 0.60 STEAM SURPLUS : 0.60 MOLES H0DE CORE HEIGHT-FT TIME-MIN FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OY.ID-HT-FRACTH 1
0.08 74.07 3684.60 3657.07 2.02 17.8 1 6.32 2
0.17 74.07
's 3654.96 3626.48 2.02 17.74 6.33 5
0.25 74.07 3625.38 3595.55 2.02 17.65 6.31 4
0.33 74.07 3595.85 3564.72 2.02 17.59 6.24 5
0.42 74.07 3566.30 3534.47 2.02 17.52 6.14 6
0.50 74.07 3536.72 3504.10 2.02 17.41 6.00 7
0.58 74.07 3507.05 3473.20 2.02 17.35 5.84 8
0.67 74.07 3477.27 3442.17 2.02 17.26 5.66 9
0.75 74.07 3447.35 3411.59 2.02 17.21 5.46 10 0.83 74.07 3417.25 3381.04 2.02 17.14 5.25 11 0.92 74.07 3386.96 3350.25 2.02 17.10 5.02 12 1.00 74.07 3356.46 3319.76 2.02 17.03 4.79 13 5.08 74.07 3325.76 3289.91 2.02 16.89 4.55 14 1 17 74.07 3294.83 3258.04 2.02 16.74 6.18 15 1.25 74.07 3263.66 3224.88 2.02 16.63 5.77 16 1.33 74.07 3232.26 3190.93 2.02 16.62 5.38 17 1.42 74.07 3200.62 3156.33 2.02 16.52 5.01 18 1.50 74.07 3168.73 3120.85 2.02 16.40 4.65 19 1.58 74.07 3136.63 3086.68 2.02 16.28 5.93 20 1.67 74.07 3104.34 3053.72 2.02 16.21 5.45 21 1.75 74.07 3071.88 3021.24 2.02 16.11 4.96 i
22 1.83 74.07 3039.27 2989.25 2.02 15.88 6.09 23 1.92 74.07 3006.45 2953.69 2.02 15.84 5.49 24 2.00 74.07 2973.46 2916,73 2.02 15.72 4.95 25 2.08 74.07 2940.31 2879.61 2.02 15.49 5. 'O 26 2.17 74.07 2907.09 2846.04 2.02 15.39
- 5. fi 27 2.25 74.07 2873.81 2813.30 2.02 15.17 4.63 28 2.33 74.07 2840.39 2776.29 2.02 14.94 5.19 29 '
2.42 74.07 2806.85 2737.85 2.02 14.67 %
4.58 I 30 2.50 74.07 2773.34 2703.94 2.02 14.41 4.95 31 2.58 74.07 2739.30 2668.83 2.02 14.05 5.18 32 2.67 74.07 2706.19 2631.18 2.02 13.59 5.24 33 2.75 74.07 2672.68 2597.59 2.02 12.97 4.47 36 N
2.83 74.07 2639.11 2559.66 2.02 12.03 4.75 33 g
2.92 74.07 2605.64 2524.03 2.02 10.27 4.40 36 3.00 74.07 2572.21 2487.47 2.02 0.0 0.0
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3.33 74.07 2438.29 2331.34 2.02 10.40 0.13 41 3.42 74.07 2402.05 2291.66 2.02 12.21 0.13 1V J
a 42
.3.50 74.07 2366.13 2252.30 2.02 13.76 0.12 43 3.58 74.07 2330.57 2213.37 2.02 15.12 0.12 44 3.67 74.07 2295.41 2174.77 2.02 16.30 0.11 45 3.75 74.07 2260.67 2136.41 2.02 17.34 0.11 46 3.83 74.07 2226.38 2098.43 2.02 18.26 0.10 47 3.92 74.07 2192.55 2060:98 2.02 19.08 0.09 48 4.00 74.07 2159.20 2023.88 2.02 19.81 0.09 49 4.08 74.07 2126.31 1987.01 2.02 20.47 0.08 50 4.17 74.07 2093.92 1950.52 2.02 21.06 0.08 51 4.25 74.07 2062.02 1914.55 2.02 21.59 0.07 52 4.33 74.07 2030.62 1878.93 2.02 22.06 0.07 53 4.42 74.07 1999.70 1843.49 2.02 22.49 0.06 54 4.50 74.07 1969.27 1808.42 2.02 22.88 0.06 55 4.58 74.07 1939.35 1773.78 2.02 23.23 0.05 56 4.67 74.07 1909.91 1739.48 2.02 23.55 0.05 57 4.75 74.07 1880.96 1705.39 2.02 23.84 0.04 58 4.83 74.07 1852.48 1671. 9 2.02 24.10 0.04 5
59 4.92 74.07 1824.50 1638.04 2.02 24.34 0.04 60 5.00 74.07 1797.01 1604.85 2.02 24.55 0.03 61 5.08 74.07 1770.08 1571.94 2.02 24.74 0.03 62
- 5. 17 74.07 ',
1743.92 1539.15 2.02 24.92 0.03 63 5.25 74.07 1718.18 1506.49 2.02 25.08 0.03 64 5.33 74.07 1692.86 1474.10 2.02 25.22 0.02 l
65 5.42 74.07 1667.93 1441.90 2.02 25.35 0.02 66 5.50 74.07 1643.39 1409.74 2.02 25.46 0.02 67 5.58 74.07 1618.86 1377.71 2.02 25.57 0.02 68 5.67 74.07 1594.76 1346.00 2.02 25.66 0.02 69 5.75 74.07
'571.16 1314.56 2.02 25.75 0.01 70 5.83 74.07 548,10 1283.24 2.02 25.82 0.01 71 5.92 74.07 iS25.57 1252.09 2.02 25.89 0.01 72 6.00 74.07 1503.59 1221.22 2.02 25.96 0.01 73 6.08 74.07 1481.84 1890.61 2.02 26.01 0.01 74 6.17 74.07 1461.04 1160.15 2.02 26.06 0.01 75 6.25 74.07 1440.76 112 9. <8 0 2.02 26.11 0.01 76 6.33 74.07 1420.97 1099.70 2.02 26.15 0.01 i
77 6.42 74.07 1401.65 1069.85 2.02 26.19 0.01 78 6.50 74.07 1382.83 1040.15 2.02 26.22 0.01 79 6.58 74.07 1364.50 1010.59 2.02 26.25 0.01 80 6.67 74.07 1346.68 981.31 2.82 26.27 0.08 81 ps) 6.75 74.07 1329.32 952.35 2.J2 26.30 0.00 82 6.83 74.07 1312.46 923.64 2.02 26.32 0.03 ps) 83 6.92 74.07 1296.11 895.18 2.02 26.34 0.00 84 IN) 7.00 74.07 1280.25 867.08 2.02 26.35 0.00 85 Jb" 7.08 74.07 1264.88 339.44 2.02 26.37 0.00 86 7.17 74.07 1250.02 812.25 2.02 26.38 0.00 87 (fa 7.25 74.07 1235.67 785.51 2.02 26.39 0.00 88 7.33 74.07 1221. 2 759.33 2.02 26.40,'
0.00 8
89 7.42 74.07 1208.52 733.84 2.02 26.41 O.00 90 7.50 74.07 1195.75 709.13 2.02 26.42 0.00 91 7.58 74.07 1183.59 685.29 2.02 26.42 0.00 92 7.67 74.07 117.1.97 662.45 2.02 26.43 0.00 93 7.75 74.07 1161.02 640.81 2.02 26.43 0.00 94 7.83 74.07 1150.80 620.54 2.02 26.44 0.00 95 7.92 74.07 1141.35 601.90 2.02 26.44 0.00 95 8.00 74.07 1132. 0 585.19 2.02 26.45 0.00 8
STEAM PRODUCED = 0.62 STEAM SURPLUS = 0.62 MOLES HDDE CORE HEIGHT-FT TIME-MIH FUEL DEG-F STEAM DEG-F FLOW RATE-LB/ HRS ZR TH-MILS OXID-HT-FRACTH 1
0.08 78.47 3452.13 3427.57 2.11 17.81 6.32
,2 O.17 78.47 3431.44 3405.56 2.11 17.74 6.33 p'
O e
3 0.25 78.47 3410.25 3382.66 2.11 17.65 6.31 4
0.33 78.47 3388.54 3359.27 2.11 17.59 6.24 5
0.42 78.47 3366.30 3335.90 2.11 17.52 6.14 6
0.50 73.47 3343.54 3311.95 2.11 17.41 6.00 7
0.58 78.47 3320.24 3287.03 2.11 17.35 5.84 4
8 0.67 78.47 3296.40 3261.53 2.11 17.26 5.66 9
0.75 78.47 3272.03 3236.02 2.11 17.21 5.46 i
10 0.83 78.47 3247.13 3210.16 2.11 17.14 5.25 11 0.92 78.47 3221.72 3183.70 2.11 17.10 5.02 12 1.00 78.47 3195.81 3157.22 2.11 17.03 4.79 13 1.08 78.47 3169.43 3131.14 2.11 16.89 4.55 14 1.17 78.47 3142.57 3103.07 2.11 16.74 6.18 15 1.25 78.47 3115.25 3073.63 2.11 16.63 5.77 l
16 1.33 78.47 3087.49 3043.27 2.11 16.62 5.38 17 1.42 78.47 3059.30 3012.09 2.11 16.52 5.01 18 1.50 78.47 3030.69 2979.77 2.11 16.40 4.65 19 1.58 78.47 3001.71 2948.31 2.11 16.28 5.93 20 1.67 78.47 2972.39 2917.71 2.11 16.21 5.43 21 1.75 78.47 2942.76 2887.46 2.11 16.11 4.96 3
22 1.83 78.47 20*?.85 2857.75 2.11 15.88 6.09 23 1.92 78.47 9 2882.65 2824.80 2.11 15.84 5.49 24 2.00 78.47 2852.17 2790.41 2.11 15.72 4.95 25 2.08 78.47 2821.44 2755.51 2.11 15.49 5.83 a
26 2.17 78.47 2790.56 2723.65 2.11 15.39 5.19 l
27 2.25 78.47 2759.55 2692.72 2.11 15.17 4.63 28 2.33 78.47 2728.35 2658.01 2.11 14.94 5.19 j
29 2.42 78.47 2696.99 2621.70 2.11 14.67 4.58 30 2.50 78.47 2665.60 2589.32 2.11 14.41 4.95 31 2.58 78.47 2634.15 2555.99 2.11 14.05 5.18 1
32 2.67 78.47 2602.60 2520.27 2.11 13.59 5.24 l
33 2.75 78.47 2571.11 2488.22 2.11 12.97 4.47 4
34 2.83 78.47 2539.55 2452.35 2.11 12.03 4.75 j
!5 2.92 78.47 2508.07 2418.43 2.11 10.27 4.40 36 3.00 78.47 2476.62 2383.69 2.11 0.0 0.0 37 3.08 78.47 2452.12 2349.33 2.11 2.47 0.09 i
38 3.17 78.47 2418.61 2312.30 2.11 5.50 0.09 39 3.25 78.47 2385.19 2275.44 2.11 8.02 0.09 40 3.33 78.47 2351.93 2238.73 2.11 10.14 0.09 41 3.42 78.47 2318.85 2202.07 2.11 11.96 0.09 42 3.50 78.47 2286.02 2165.63 2.11 13.52 0.08 43 3.58 78.47 2253.48 2129.52 2.11 14.88 0.08 44 3.67 78.47 2221.24 2093.66 2.11 16.08 0.08 45 3.75 78.47 2189.33 2057.95 2.11 17.13 0.07 46 3.83 78.47 2157.78 2022.53 2.11 18.07 0.07 l
47 3.92 78.47 2126.60 1987.51 2.11 18.90 0.06 48 4.00 78.47 2095.81 1952.78 2.11 19.64 0.06 49 4.08 78.47 2065.41 1918.23 2.11 20.31 0.06 50 4.17 78.47 2035.42 1883.95 2.11 20.91 N 0.05 51 4.25 78.47 2005.84 1550.11 2.11 21.45 0.05 52 4.33 78.47 1976.69 1816.56 2.11 21.94 0.05 53 p
4.42 78.47 1947.95 1783.16 2.11 22.38 0.04 54 4.50 78.47 1919.63 1750.04 2.11 22.77 0.04 N
55 4.58 78.47 1891.76 1717.29 2.11 23.13 0.04 53 N
4.67 78.47 1864.30 1684.84 2.11 23.46 0.03 Si A
4.75 78.47 1837.29 1652.57 2.11 23.75 0.03 4.83 78.47 1810.70 1620.56 2.11 24.02 0.03 56 u
4.92 78.47 1784.56 1588.74 2.11 24.26 0.03
. 59 e
60 5.00 78.47 1759.13 1557.25 2.11 24.48 0.02 61 5.08 78.47 1734.25 1525.97 2.11 24.68 0.02
- 5.17 78.47 1709.77 1494.74 2.11 24.86 0.02 62
63
.5.25 78.47 1685.64 1463.63 2.11 25.02 0.02 64 5.33 78.47 1661.90 1432.75 2.11 25.17 0.02 65 5.42 78.47 1638.42 1402.05 2.11 25.30 0.02 66 5.50 78.47 1614.92 1371.44 2.11 25.42 0.01 67 5.58 78.47 15 91. <81 1341.01 2.11 25.53 0.01 68 5.67 78.47 1569.21 1310. <58 2.11 25.63 0.01 69 5.75 78.47 1547.10 1281.03 2.11 25.72 0.01 70 5.83 78.47 1525.49 1251.33 2.11 25.80 0.01 71 5.92 78.47 1504.39 1221.')
2.11 25.87 0.01 7
72 6.00 78.47 1483.48 1192.49 2.11 25.93 0.01 73 6.08 78.47 1463.52 1163.49 2.11 25.99 0.01 74 6.17 78.47 1444.08 1134.63 2.11 26.05 0.01 l
75 6.25 78.47 1425.10 110 5. <8 9 2.11 26.09 0.01 76 6.33 78.47 1406.60 1077.38 2.11 26.13 0.01 77 6.42 78.47 1388.53 1049.13 2.11 26.17 0.01 78 6.50 78.47 1370.95 1021.06 2.11 26.21 0.01 79 6.58 78.47 1353.82 993.15 2.11 26.24 0.00 83 6.67 78.47 1337.17 965.50 2.11 26.26 0.00 81 6.75 78.47 1320.96 935.19 2.11 26.29 0.00 82 6.83 78.47 1305.23 911.15 2.11 26.31 0.00 83 6.92 78.47
's 1289.96 384.39 2.11 26.33 0.00 84 7.00 78.47 1275.17 858.00 2.11 26.34 0.00 85 7.08 78.47 1260.84 832.05 2.11 26.36 0.00 6
86 7.17 78.47 1247.00 806.59 2.11 26.37 0.00 i
87 7.25 78.47 1233.64 781.61 2.11 26.38 0.00 88 7.33 78.47 1220.76 757,19 2.11 26.39 0.00 8
89 7.42 78.47 1208.40 733.47 2.11 26.40 0.00 90 7.50 78.47 1196.55 710.52 2.11 26.41 0.00 91 7.58 78.47 1185.29 688.44 2.11 26.42 0.00 92 7.67 78.47 1174.55 667.38 2.11 26.43 0.22 I
95 7.75 78.47 1164.46 647.49 2.11 26.43 0.00 i
94 7.8' 78.47 1155.0-8 628.97 2.11 26.44 0.00 j
95 7.92 78.47 1146.44 612.06 2.11 26.44 0.00 e
96 8.00 78.47 1138.69 597.06 2.11 26.44 0.00 l
STEAM PRODUCED : 0.65 STEAM SURPLUS : 0.65 MOLES TOTAL HYDROGEN GENERATED =0.1898E+01 MOLES IWARN :
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PANEL 1 FRAME 1
FUEL TEMPERATURE HISTORIES OF 1 FT HODES l
5000l+-------+-------+-------+-------+-------+-------+-------+-------+-------+-------+
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+-------+-------+-------+-------+-------+---^---+--1111-+----- '11----0.+-------+
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JP" TIME - MINUTES L/d f.
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