Numerical simulation for a one well
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Numerical Simulation of Individual
Field Simulation Model
AL I M. AK B AR
M. D. ARNOLD
A. HERBERT HARVEY
MEMBERS SPE.AIME
I
KUWAIT U,
KUWAIT
I
U. OF MISSOURI –ROLLA
ROLLA, MO.
Wells in a
INTRODUCTION
Pressures and fluid saturations in hydrocarbon
reservoirs may be described at any point by
differential equations involving reservoir rock and
fluid properties. Numerical simulation of field
performance is accomplished by establishing some
type of reference grid, writing the appropriate
equations for each mesh poirrt, then solving the
system of equations by a finite-difference t~chnique,
Since the number of mesh points must be finite,
there is a necessary assumption that each mesh
point is representative of a finite segment of the
reservoir. Actually, however, pressures are not
equal throughout such a segment of a producing
field.
This inequality of pressures within an
element of the reference grid creates problems when
the element contains a production or injection well.
Since the finite-difference technique calculates a
pressure that is representative of the entire element,
this pressure is not the bottom-hole pressure of the
well. This situation will exist even though the well
location may coincide with the grid point used to
represent the element.
Furthermore, this characteri-
stic of the finite-difference approximation is not
unique to the pressure calculation. Fluid saturations
computed for a mesh point actually repesent
saturations of a finite segment of the reservoir.
Fluid produced from the area of the wellbore is
handled mathematically as if it were withdrawn from
the entire area associated with a mesh point. Since
the conventional finite-difference technique does not
adequately describe reservoir conditions near a
well, .sPecial mathematical techniques are required
to handle the problem.
AVAILABLE TECHNIQUES
Several methods have been employed to predict
well bottom-hole pressure for numerical simulation
work.
Attempts to use mesh-point pressure as
bottom-hoJe pressure were generally unsatisfactory
Original manuscript received in Society of
Petroleum Engineers
office Sept. 5, 1972. Revised manuscript received Jan, 10, 1974.
Paper (SPE 4073) was first presented at the SPE-AIME 47th
Annual Fall Meeting, held in San Antonio, Tex., Oct. 8-11, 1972.
@ Copyright 1974 American Institute of Mining, Metallurgical,
and Petroleum Engineers, Inc.
lr?eferences listed et end of paper.
AI’ GI’ST ,1974
for reasons previously discussed. A more useful
technique is to reduce permeability arbitrarily at
mesh points corresponding to producing wells, thus
obtaining mesh-point pressures that correspond to
estimated bottom-hole pressures. It has also been
suggested that it might be possible to represent
pressure distributions by means of piecewise-
polynomial approximations.l The technique involves
the use of high-order polynomials to represent the
immediate vicinity of the wellbore. and lower-order
polynomials to represent points more remote from
the well.
Another procedure that has been used with some
success is to estimate bottom-hole pressure by
extrapolating pressures from grid blocks adjacent
to the block in which the well is located. The
extrapolation is based on Darcy’s law written in
radial form and
integrated
for
steady - state
conditions. The result of this integration may be
written
BHP . pa –
~oBoPo ‘n ‘ r i , j i rw )
2rrk k ,. b
where is the average pressure
,. ...
1)
on the edges of
grid blo;k, and ri, i is ‘the radius of a hypothetical
circle with an area equal to that of the grid block.
Although Eq, 1 is entirely adequate for estimating
bottom-hole pressure in some instances, it can lead
:0 erroneous results under unfavorable conditions.
For example, a well with a large drawdown below
bubble-point pressure
may generate a high gas
saturation in the vicinity of the borehole. This
change in saturation reduces relative permeability
to oil near the wellbore. Since the areal model does
not account for this effect and the extrapolation
technique uses the saturation computed by the areal
model, this approach may predict a bottom-hole
pressure that is too high.
Another approach to the simulation of performance
near a well has been described by MacDonald and
Coats2 and by Letkeman and Ridings.3 Techniques
described by those authors use radial coordinate
grids to solve the problems of gas coning and water
coning at individual wells. Since these computa-
tional methods have proved to be useful in solving
coning problems,
it seems logical to extend the
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ideas by combining the radial simulation of
individual wells with the conventional rectangular-
coordinate simulation of multiwell reservoirs. This
study presents the results of such a simulation.
DEVELOPMENT OF THE MODEL
The mathematical model developed by the authors
incorporates
a radial coordinate well simulator
within a two-dimensional, three-phase, Cartesian
coordinate reservoir simulation model. This areal
model is essentially a conventional numericai
simulator that provides for variable g,ritl spacing,
and accounts for effects of relative permeability,
reservoir heterogeneity, anisotropy, and structural
dip.
The well simulator is a one-dimensional, three-
phase, radial coordinate
model
emplo; ed
automatically
for those wells that have been
selected for detailed analysis. The radial modei
was based on the equation
However,
since the circular shape of the radial
model corresponds more closely to a square than to
a rectangle, this study was made with Axi = AYj for
grid blocks that contain wells. The use of square
grid blocks near producing wells is consistent with
conventional modeling techniques. We customarily
use rectangular grid spacing only to represent the
reservoir system at points remote from the area of
primary interes t.
We have not endeavored to determine the maximum
deviation from a square grid pattern that can be
successfully employed with this technique. Until
such an investigation has been made, it is suggested
that the method be used only with square or nearly
square) grid systems,
Another criterion selected to assure correspond-
ence of the two models is that the volumetrically
weighted average pressure within the radial model
equal the corresponding block pressure in the areal
model. Since accumulated round-off error could
2 9
eventually cause a discrepancy in pressures
Bo-f3 R )
calculated by the two models, pressures in the
~ “s or f30po
radial model were automatically adjusted to maintain
s
M.
s
113
r
q
c, 4
s ’
c,’, -
—0 — -
2 .-4’
/30 d ’
Bg
dP
so f3 ,
)
J/>
,—. - —.
B“dl ’ ””””’
) I
. . . . .
2)
To minimize discretization error, it was considered
desirable to use uniform increments in the discretized
equation
.4 However, to minimize computation time,
a fine grid spacing should be used only near the
wellbore, where pressure gradients are large. This
problem was resolved by transforming Eq. 2
according to the relationship s = in r. The resulting
equation was discretized with constant ,1s, thus
achieving both uniform increments of the spatial
variable
and a grid
spacing
that
increases
logarithmically with distance from the wellbore.
Ten radial grid segments were used in this study.
Since the radial model represents a rectangular
or square) grid block in the areal model, it was
necessary to establish criteria for equivalence of
the two systems. One criterion is that the pore
volume of the radial model must equa~ the pore
volume of the rectangular block. Since porosity and
bed thickness in the radial model equal the
corresponding terms in the areal model, the radius
of the well simulator was calculated by
—..
ri j : ~’,lxi.Ayjj’rr, . . . . . . . . . . . . 3)
.
The effect of relative sizes of Axi and Ayj on
accuracy of the simulation has not been investigated.
316
the desired equivalency with areal model pressure.
These small adjustments were made without altering
the pressure gradients calculated by the radial
model.
If the radial model is to represent the system
predicted by the areal simulator, then the fluid
fluxes must be the same for both models. This
condition was achieved by summing the fluxes into
the four vertical faces of the grid block in the areal
model, and considering the total flux for each phase
as influx into the closed outer boundary of the
radial model. It should be noted that small errors in
calculating pressures in
the areal model may
invalidate the flux calculation. Thus it is essential
that pressure residuals in the areal model be quite
low. Several approaches to reduction of residuals
were investigated. One method that was found to
converge rapidly even for highly heterogeneous
reservoir conditions
was the strongly implicit
procedure. 5 ‘
Pressures,
saturations,
and ner oil flux were
calculated by the areal modeI on the basis of oil
production rates that were fixed by computations
external to the model. The total oil rates were
computed by Darcy’s law on the basis of the
gradients
calculated by Eq. 2. All relative
permeabilities were baxed on the upstream fluid
saturations. Water and gas fluxes were determined
in the same manner as the oil flux. It was assumed
that all phases would flow toward the producing
weJ1. Although it is possible for counterblow to
occur in
an oil reservoir,
the assumption of
unidirectional flow is usually valid near a producing
well.
The next step i;, the calculation procedure was
to compute pressures, saturations, and oil production
rate from the radial model.
The volumetrical ly
averaged pressures in the two models were then
compared, and adjusted if required in the radial
model to maintain equality. Water and gas production
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rates from the radial model were then determined
from Darcy’s law,
and production rates for this
model were compared with corresponding flax rates
predicted by the areal model. If any of these rates
were found to differ significantly in the two models,
areal model pressure calculations were repeated
using production rates calculated by the radial
model. This iterative process was repeated until
the two models predicted the same fluid production
rates. Convergence was frequently achieved during
the first computation, with no iteration.
This rapid convergence can be attributed to the
fact that production rates seldom changed signifi-
cantly during a time step. The maximum time
increment used during the simulation was 90 days.
Since the production rates changed slowly, accurate
prediction of these rates for the subsequent time
step could usually be achieved. The predicted
production rates for the areal model were computed
on the basis of the values of Elo, PO,
kfo,
and
potential gradients that were calculated from
pressures
and saturations predicted for the new
time step by extrapolation in the radial model,
It should be noted that the method of computation
can lead to an ambiguous situation. The radial
model may predict the production of free gas while
the areal model indicates that the block pressure is
greater than bubble-point pressure. This situation
arises because the areal model fails to provide an
adequate
simulation
of reservoir conditions near the
wellbore. The problem was handled by comparing
free gas production predicted by the two models.
Any excess gas predicted by the radial model was
considered as additional solution gas production in
the areal model. Since the material balance must be
maintained in each model, ??~ in the areal model
was
reduced to account for rhis excess gas
production.
APPLICATION OF THE MODEL.
The model has not yet been tested against actual
field performance .
However, tests that have been
conducted indicate that the technique is successful
in combining individual well simulation with the
numerical simulation of an entire reservoir. Table 1
describes a small hypothetical oil field that has
TABLE 1 —
DATA FOR SIMULATION OF HYPOTHETICAL
OIL FIELD
POrO~ity, percent
20
Permeabi li ty, md
50
Thickness, ft 20
Initial water saturation, Well s 1 ond 2, percent 18
Initial reservoir pressure at -6,130 ft, psia
2,855
Bubblepoint pressure, psio
2,172
Oil viscosity at initial reservoir conditions, CP
1.08
Initial soluticm GOR, cu ft /bbl
.573
Reservoir pore volume, million bbl 19.86
Natural woter inf lux
None
Allowoble production rote, B/D/well 197
Water iniection rote, B/D
300
Well radius all wells), in, 5
Number of grid blocks for areal model 10X 10)
100
Size of grid blocks for oreal model
528 ft
X
528 ft
Critical gas soturotion, percent 8.9
been
studied.
The reservoir is homogeneous,
isotropic, and uniformly thick. As illustrated by
Fig.
1, development consists of two producing
wells, one water injection well, and sufficient dry
holes to define the limits of the field. Water
injection is begun 3 years after first production,
Since the injection rate exceeds the production rate,
a gradual ~ncrease in both reservoir pressure and
p:oducrivity index occurs.
The method used to determine production rrtes
requires some discussion. Calculation of these
rates for a mathematical model requires data that
are not included in the differential equations upon
which the model is based. Pertinent considerations
include production method flowing or artificial
lift), proration regulations, separator pressures,
tubing size, etc. Almost invariably, one or more of
these factors will be altered during the depletion of
the reservoir. The relationship between bottom-hole
f]owing pressure and production rate may be
described by an IPR curve. b Although the curve can
be linear, factors such as reservoir stratification
and changes in relative permeability usually cause
significant deviation from a straight line.
Since the problem of predicting well productivity
pertains only indirectly to this study, a simplified
method for specifying production rates was used.
For this example it was assumed that both Wells 1
and 2 would produce at the allowable rate until
TABLE 2 —
RELATIVE PERMEABILITY
so
k
ro
0.18
0
0.20
0.00003
0.25
0.00058
0.30
0.00237
0.35 0.00640
0.40
0.01404
0.45
0.02711
0.50
0.04788
0.55
0.0792
0.60
0.12450
0,65
0.18785
0.70
0.27405
0.75
0.38866
0.80
0.53806
0.82
0.60916
Water saturation = 18 pe, cer,t.
k
rd
0.22126
0.19803
0.14719
0.10590
0.07315
0.04797
0.02935
0.01630
0.00784
0.00297
0.00070
0.00002
0
0
0
Pressure
psio)
200
400
600
800
1,000
1,200
1,400
1,600
1,800
2,000
2,172 BP)
2,400
2,600
2,855
TABLE 3 — FLUID PROPERTIES
Formation
Viscosi ty cp)
Volume Factor
Solution Gas
Oil
Go S
‘Oil
GO;
scf/STB)
—. —
2.0989 0.010
1.0465 0.073S
74.6
1.9649 0.011
1.0675 0.0368
125.2
1.8371
0.012
1.0931 0.0245
175.8
1.7155 0.013
1.1216 0.0184
226.4
1.6000 0,014
1.1580 0.0144
277.0
1.4910 0,015
1.1973 0,0119
327,6
1.3875 0.016
1.2411
0.0096
378.2
1.2905 0.017
1.2895 0.04)83
428.8
1.1997 0,018
1.3425 0.0073
479.4
1.1150 0.019 1.4000 0.0065
530.0
1,0471 0.0199 1.4531 0.0054
573.5
1.0585 0.021
1.4481 0.0053
573.5
1.0685 0.022 1.4438 0.0049
573.5
1,0813 0.0233 1.4383 0.0045
573.5
41’ G1’ST. 1974
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/
\
\
\
\
\
\
\
‘
00
Contouredonlop
of productive
formotnon
. otl well
0 vfoter,nject,on well
0
500
FIG. 1 —STRUCTURAL MAP OF HYPOTHETICAL OIL
FIELD.
30
20
t,. 0.?04
yeot
___ Ateol Model
tp = 04136
yOOf
_ Combmmd Areal and
RodmiNadele
/3 : 062
yoof
t4= )52
years
t 5 : 301
years
16:50
ywrs 2y80r s a ft er ft rs t m ject tm )
“o
100
200
300
400 500
DISTANCE, FEET
FIG.
2 — CALCULATED DISTRIBUTION OF GAS
SATURATION.
?400
1
\
moo
I,
:
\
\
: \
s
,600
\
:
\
\
--- A.,. ..4,3
\
:
— co b . . ...8 ..d . , 6. . 4 . 0, *
? (200
\
\
i
\\
s
\
~ \
800
\
g
L.
~.
;,,.,?., .0,,,,., fl,w
-.”
~ 4
_ _
J__.__J ‘
1
2 3
4
5
,,”f. “fans
FIG. 3 — CALCULATED PRODUCING BOT’IY)M-HOLE
PRESSURE, WELL 1.
318
bottom-hole pressure was reduced to 200 psia.
Thereafter, bottom-hole pressure remained constant,
and production rates declined accordingly. To
provide a basis for comparison, reservoir perform-
ance was calculated both with and without radial
simulation of the two producing wells. Use of the
radial simulator increased computation time by
approximately 15 percent. The areal model used for
comparison included an extrapolation technique for
estimating bottom-hole pressure.
Although the same criteria were i.sed to determine
reservoir behavior for the two metho.~s of simulation,
significant differences
in predicted reservoir
performance
were
observed. As illustrated by Fig.
2, the combined radial and areal models predict an
early buildup in gas saturation near the production
wells, whereas the areal model without the radial
simulator does not anticipate this effect. Figs. 3
and 4 depict rhe producing bottom-hole pressure and
productivity index, respectively, as calculated by
the two types of simulation models. Fig. 5 indicates
the calculated pressure distribution in the vicinity
of Well 1. The increase in reservoir pressure that
occurs during the fourth and fifth years is a result
of water injection in Well 3. Oil production rates
and calculated GOR are illustrated by Figs, 6 and
7, respectively.
CONCLUSIONS
Individual well simulation can be included in the
mathematical model of a hydrocarbon reservoir. The
increase in computer time required for running such
a model is not excessive,
provided that a one-
03
G
n
:
<
0
lx
w
a
-J 02
m
o
, fr ons en t per f od
b= m
I
I
I
___ Areol Model
I
_ Comb,ned Areal ond ROdml Mode
\
\
\
IStorl of Wofer
I
I
I
I
o
I
2
3
4
5
TIME, YEARS
FIG. 4 — CALCULATED PRODUCTIVITY
INDEX,
WELL 1.
sOCIEIY
OF PET ROI.};I” M EX(;13EKI{> ]01’RSAL
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dimensional well simulator is used. It is suggested
that this type of model be employed to study
reservoirs where pressure drawdown at producing
wells is large, and bottom-hole pressure is less
than bubble-point pressure.
BHP =
B=
‘- =
g.
h=
i=
j=
k=
k, =
pa .
pg .
p. .
Pfu =
q.
9gf =
T
.
R. =
s.
5.
t=
x=
Y=
z
P=
2800
2400
2000
~
f
Iuoo
2
;
: 1200
n
800
NOMENCLATURE
bottom-hole pressure at producing well
formation volume factor
compressibility
acceleration of gravity
thickness
subscript used to denote position on x-
coordintite axis
subscript used to denote position on y-
coordinate axis
permeability
relat ive permeabili ty
average pressure at edges of grid block
pressure in gas phase
pressure in oil phase
pressure in water phase
production rate
free gas production rate
radial dis tance
solution gas/oil ratio
in r
saturation
time
space coordinate for areal model
space coordinate for areal model
depth
viscosity
,
i
yeor s smw mttl al
productmn
w , l l No I
J
ml
200 300 400
300 m
DISTANCE, FEET
FIG. 5 — CALCUJ-ATED PRJ==URE DISTRIBUTION
FROM COMBINED AREAL AND RADIAL MODELS.
AI’(; I”s T,197\
p =
density
@ = porosity
@g = gas
potentiaI, pg - pggz
@o = oil potential, p. - pogz)
@w = water potential, pw -
pwgz
SUBSCRIPTS
1.
2.
3.
g =
gas
o = oil
w = water
REFERENCES
Cavendish, J. C., Price, H. S., and Varga, R, S.:
“Galerkin Methods for the Numerical Solution of
Boundary Value Problem s,” Sot. Pet. .Eng. J. (June
1969) 204-220; Trans., AIME, Vol. 253.
MacDonald, R. C,, and Coats, K. H.: “Methods for
Numerical Simulation of Water and Gas Coning, “ Sot.
Pet. f?ng. J. (Dec. 1970) 425-436; Trarzs., AIME, Vol.
249.
Le keman, J. P., and Ridings, R, L.: “A Numerical
Coning Model, ” Sot. Pej. .@n j. (Dec. 1970) 418-424;
Trans., AIME, Vol. 249.
200
0
a
o
‘. 150
w
s
a
0
Well No. I
—.— Well No. 2
I ---——- -
stort of woh?r reject/on I
I
o
I
2
3
4
5
TIME, YEARS
FIG. 6 — OIL PRODUCTION RATES.
start of wofer injecflon
I
--e+y
riginol
I
solution
GOR
(S74)
-/
200
0
I
2
3
4 5
TIME , YEARS
FIG, 7 —
CALCULATED GOR, WELL 1.
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4. Settari, A., and Aziz, Khalid: “Use of Irregular Grid
in Reservoir Simulation, ” Sot.
Pet. Eng. ].
(April
1972) 103-114.
6.
5, Stone, Herbert L.:
“Iterative Solution of Implicit
Approximations of Multidimensional Partial Difference
S20
SO CIE”I’Y OF PET ROLEIIM EN GISEERS JO CRXAL