Dynamic hydrocarbon trapping and implications for seal ... · fault zone to lead to a rise of 100m...
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Dynamic hydrocarbon trapping and implications for seal analysis
Christopher A.J. Wibberley (Total)
Vertical and lateral seals are often assumed to be static, with a fixed seal threshold determined by capillary
properties. When fault seals are considered in this context, the buoyancy pressure of the hydrocarbon column
is retained by the capillary membrane properties of the water-saturated fault zone. If trap filling continues
until the buoyancy pressure rises beyond the fault capillary threshold pressure, excess hydrocarbons are bled
off into the fault zone and may flow across and/or up the fault. In this way, the trappable hydrocarbon column
buoyancy pressure is always limited by the seal capillary threshold pressure, and estimates of fault capillary
threshold pressure are one way of evaluating trappable column heights in fault-bounded prospects.
Lookback analysis is often used to catalogue hydrocarbon column heights (or buoyancy pressures) trapped
against faults as a function of lithological-based parameters such as the shale-gouge ratio (SGR, Yielding et
al., 1997). These catalogues constrain algorithms which provide another way to predict maximum trappable
column heights in prospect evaluation. This presentation firstly reviews an example showing how lookback
analyses were used to compile algorithms for fault seal prediction in normally-pressured traps. However,
lookback analyses of nearby case studies of overpressured hydrodynamic traps do not fit these algorithms.
Furthermore, in active hydrodynamic environments vertical and lateral pressure cellularisation is common,
and significant pressure differences may exist across faults even in single-phase scenarii where capillary
trapping cannot be an issue. The key parameter here is therefore the permeability of the seal. Similarly, for
hydrocarbon columns which leak into fault zones when buoyancy pressure of the hydrocarbon column attains
the capillary threshold pressure, a continuous pathway of hydrocarbon through the membrane will lead to
relative hydrocarbon permeability close to that of single-phase flow. Continued active charge faster than the
leak rate will result in a larger column trapped against the fault, controlled largely by fault zone permeability.
The question then arises of whether the permeability of a fault zone can be sufficiently low to trap significant
column heights on the geological timescale (seal permeability is generally only considered important in
production contexts). This question is addressed by calculating how long it would take for leakage across a
fault zone to lead to a rise of 100m in free-water level (FWL) in a fault-bounded trap. Results in Figure 1
suggest that in some cases clay-rick fault zones can reduce the leak rate of Darcian flow of hydrocarbons on
sufficiently long timescales for this to be an important seal mechanism in active hydrocarbon basins.
Figure 1: Simple geometrical model for a fault-bounded trap with leak induced by an aquifer pressure potential gradient, with
results of calculations for the time taken for a 100m rise in FWL.
Examples are presented which demonstrate the use of applying such quantified hydrodynamic concepts in
predicting (1) aquifer pressure potentials in undrilled compartments, (2) charge rates into prospects across and
up faults and hence likelihood of fill-to-spill from active charging through faults, and (3) likelihood of
differences in fault sealing behavior between exploration and production timescales, important for identifying
possible compartmentalization during field development and production.
The first example, from the Caucasian region, is a direct application of hydrodynamic principals to prospect
evaluation (Figure 2). A pressure potential gradient is evidenced by two wells spaced around 10 km apart
(wells A and B in Fig. 2a), assuming laterally continuous reservoir properties. The lower-pressure well (well
B in Fig. 2a) is on one side of a faulted 4-way closure, but was water-bearing despite regional hydrocarbon
migration being thought to have followed the pressure potential gradient from the basin centre to arrive
against the fault in this 4-way closure. A prospect was defined in the same 4-way closure but on the other side
of the fault (prospect C in Figure 2a), with prospect evaluation relying heavily on aquifer pressure prediction
with a similar reasoning to that of hydrodynamic drive (Grauls et al., 2002; Grosjean et al. 2009). However,
this prospect did not have any nearby calibration wells for the reservoir aquifer pressure. The nearest well on
the same side of the fault was a further 30 km away towards the edge of the basin (well D in Figure 2a) and
close to hydrostatic pressure, suggesting either of two end-member scenarii: (1) a significant drop in reservoir
pressure potential across the fault, or (2) no or little pressure drop across the fault, but instead, a continuous
degradation in reservoir poroperm properties or reservoir continuity towards the edge of the basin.
Figure 2: (a) Sketch of the geological scenario of pressure potential (Ppot) decrease from basin centre (close to well A) to basin
edge (close to well D) including a strong pressure potential drop across the faulted 4-way closure in which well B and the
prospect are situated; (b) Darcian flow calculations for assessing the fault permeability required to explain the across-fault
pressure potential drop in scenario (1).
Prior to drilling the prospect no direct petrophysical data were available to distinguish between the two
possibilities. However, as in the first example, the question was asked “what fault permeability would be
required to explain the across-fault pressure potential drop assumed in scenario (1) ?” A simple 1-D steady-
state aquifer flow model is used (Figure 2b), assuming that the flux in (Qn) equals flux out (Qn+1), in each of
the flow units in Fig. 2b. From Darcy’s Law the problem can be reduced to one of a ratio of reservoir
permeability to fault permeability, for a given pressure potential decrease across the fault. The pressure
potential decrease across the fault in scenario (1) would require an across-fault permeability in the range
0.03µD to 0.3µD for a fault zone thickness from 1 to 10m. The impact of this calculation is two-fold. Firstly,
this range of values falls right on the range of across-fault permeability values predicted by Total’s fault
permeability algorithm for the SGR range of 30 – 50% estimated from well B, thus providing another
validation point for the algorithm. Secondly, the fact that the fault permeability values are thought to be
reasonable suggests that scenario (1) is likely to be the more appropriate one. This interpretation was
successfully tested when the prospect was drilled and found to contain a hydrocarbon column compatible with
the aquifer pressures suggested by scenario (1).
A dynamic context can also be created artificially during production by reservoir pressure depletion on one
side of a fault. Lookback analyses of exploration well pressure and contact data can often give a misleading
impression of how such fault seals may behave during production. This is because the long-term context of
fluid pressure distribution and possibly stabilized hydrocarbon charge may not reveal information on how
such seals could behave due to the introduction of a short-term, transient instability. The second example, of a
Tertiary turbidite field in conventional offshore W. Africa, is a case of potential compartmentalization by
anticline crestal-collapse faults not being recognized by exploration wells because identical pressure trends
and a communal OWC were detected across the field. Despite this, the distribution of pressure depletion after
production start-up suggests that this fault is causing a production timescale compartmentalisation effect. This
effect has been confirmed as being due to the fault both by pressure data in a later well drilled across the fault,
and by the 4-D signal which shows a break at the fault itself. This change in apparent fault seal behaviour can
be explained simply by the fault transmissibility from reasonable across-fault permeability values (Figure 3).
Figure 3: A pulse in across-fault pressure gradient by instantaneous charge or drawdown on one side of the fault, and the fault
permeabilities required to re-equilibrate the gradient over a given timescale.
Figure 3 examines the range of values of across-fault permeability required to produce this effect, with the
production timescale (~ 10 years) being too short to allow pressure re-equilibration which can nevertheless
occur over a long (geological) period of time (e.g. 100,000 to 10 million years). From simple 1-D flow
calculations, across-fault permeability values in the micro to sub-microDarcy range match this scenario
(Figure 3). Such a fault permeability range lies in between published values of fault permeability for fault
zones in purely sand-rich contexts and those with a high clay content (e.g. Wibberley & Shimamoto, 2005;
Saillet & Wibberley, 2013). Given the turbiditic depositional environment of the reservoirs, an “intermediate”
proportion of clay is expected in the fault zone, even without performing a detailed shale gouge ratio
calculation. This apparent match between calculation results and expected fault permeability from published
data provides support for the hypothesis proposed of the transient sealing behaviour of the fault during field
production.
Conclusions
Advances in quantifying fault zone permeability in the last few years allow us to test hypotheses for dynamic
flow through faults over geologically short and long timescales. It is shown here how this helps in
understanding seal mechanisms in lookback analyses as well as prediction of trapped hydrocarbon columns
and aquifer pressure distributions in hydrodynamic settings. For short timescales, production well data may
appear to diverge from initial pre-prod conclusions drawn from exploration well results. However, our
knowledge of fault permeability along with the help of simple calculations are used to show how these
apparent differences in behaviour do not conflict, but rather improve, our understanding of fault seal
behaviour. These case studies illustrate Total’s ability to accelerate the application of R&D results to
exploration studies through integrating structural geology and petrophysics in basin evaluation.
Acknowledgements
The authors wish to thank TOTAL for permission to publish the work.
References
Grauls, D., Pascaud, F. and Rives, T. 2002. Quantitative fault seal assessment in hydrocarbon-
compartmentalised structures using fluid pressure data. In: Hydrocarbon Seal Quantification. A.G. Koestler
and R. Hunsdale (eds.), NPF Special Publication 11: 141 – 156.
Grosjean, Y., Zaugg, P. and Gaulier, J.-M. 2009. Burial Hydrodynamics and Subtle Hydrocarbon Trap
Evaluation: from the Mahakam Delta to the South Caspian Sea. Paper presented at the International Petroleum
Technology Conference, 7-9 December 2009, Doha.
Saillet, E. and Wibberley, C.A.J. 2013. Permeability and flow impact of faults and deformation bands in high-
porosity sand reservoirs: Southeast Basin, France, analog. AAPG Bulletin, 97: 437–464.
Wibberley, C. A. J. and Shimamoto, T. 2005. Earth-quake slip weakening and asperities explained by thermal
pressurization. Nature, 436: 689–692.
Yielding, G., Freeman, B. and Needham, T. 1997. Quantitative fault seal prediction. American Association of
Petroleum Geologists Bulletin, 81: 897–917.
© Marc Roussel / Total
DYNAMIC HYDROCARBON TRAPPING and implications for seal analysis
Christopher WIBBERLEY, TOTAL
- Fault zone seal composition
- Examples of seal lookback analyses
- Static seal threshold pressure approach
1) LOOKBACK ANALYSES: HYDROSTATIC VS. OVP CONTEXTS
assumed to = % shale within the fault zone
SHALE GOUGE RATIO (SGR): CONCEPT
Throw
%Vcl1 . ∆t1
%Vcl2 . ∆t2
%Vcl3 . ∆t3
%Vcl4 . ∆t4
%Vcl5 . ∆t5
SGR = average Vcl past which a point has slipped
SGR = Sum [Vcli . ∆ti]
Throw
A
A’ B
B’
One SGR value per point
3
Siliclastic host series
FAULT SEAL THRESHOLD: EXAMPLE OF LOCAL CALIBRATION
Local calibration
• Cases where gas-bearing reservoirs forming the trap are juxtaposed against water-bearing reservoirs.
Threshold of maximum column heights
“Local” calibration based on a specific zone, using > 30 cases gas columns trapped against faults
FAULT SEALED COLUMNS IN AN OVERPRESSURE CONTEXT
5
• Cases where gas-bearing reservoirs forming the trap are juxtaposed against water-bearing reservoirs.
OVP cases Hydrostatic cases
Overpressured contexts: fault seal behaviour follows different rules
CAPILLARY SEAL CONCEPT – APPLICATION TO TOPSEAL
r
seal
reservoir Phc
Pe Pe
Pw
Hc Hc FWL
θ
Hc(max)
Fluid pressure
Dep
th
6
Phc Pe Pw
Hc Hc(max)
Phc
FWL
Hc Phc
Pe Pw
Hc Hc(max)
FWL
Hc Hc(max)
Phc
Pe Pw
Hc
FWL
Hc
Phc = (ρw- ρhc).g.H Pe : Capillary entry pressure
Pe = 2 *IFT*cos θ / r
Phc : HC-induced buoyancy effect
>
Cap rock Capillary leakage whenever: Phc > Pe
CAPILLARY SEAL CONCEPT – APPLICATION TO FAULTS
Phc(top) Pe(top) Pw
Fault entry pressure profile Topseal entry
pressure profile Phyllosilicate-rich fault zone of complex internal structure
Hc Fault zone water
saturated?
7
Hc FWL
Topseal
Fault seal
Phc(top)
Pe(top) Pw
Fault entry pressure profile Topseal entry
pressure profile Phyllosilicate-rich fault zone of complex internal structure
Fault zone water saturated?
Hc
FWL
Topseal
Fault seal
Hc
Phc(top)
Pe(top) Pw
Hc
FWL
Topseal
Fault seal
Fault entry pressure profile Topseal entry
pressure profile
Pe(FLP)
Phyllosilicate-rich fault zone of complex internal structure
Hc(max)
Hc(FLP)
Fault zone water saturated?
At Fault Leak Point (FLP): Pe(FLP) = (ρw – ρhc).g.Hc(FLP) Can not explain aquifer ∆Ppotential !
2) NEW APPROACHES : PERMEABILITY AND OVERPRESSURE
from Grauls et al. (2002)
Hc flushed through the fault Hc column “sealed” by aquifer pressure
Top Seal
Pw 2 Pw 1
∆Hc
F1 Channel OWC 1
OWC 2
Pw 2 Pw 1
∆ppot (aq) ∆ppot(aq) = ∆ρ. g. ∆Hc
Pressure equilibrium across the fault ρoil
ρaq
∆ρ = ρaq - ρoil
Pressure
Case study of pseudo-static Hc response to maintaint across-fault pressure equilibrium
HYDRODYNAMIC DRIVE THROUGH OVP
FAULT COMPARTMENTS : CENTRAL
NORTH SEA CASE 5
5 6
4
3 2
1
HYDRAULIC FRACTURE REGIME
NORMAL HYDROSTATIC PRESSURE REGIME Pressure (bars)
400 500 600 700
Dep
th (m
/sl)
3400
3600
3800
4000
S3
WEST EAST
From M. Sacleux & D. Grauls
‘DYNAMIC’ CONCEPTS: PERMEABILITY OF A FAULT SEAL
Presentation title - Place and Country - Date Month Day Year 10
1
100
10 000
1 000 000
100 000 000
1 10 100
1 mD
0.1 mD
10 µD
1 µD
0.1 µD
10 nD
1 nD
Clay-richfault gouge
Quartzo-feldsp.fault gouge
V(FWL)
θf θs d
A V(fault)
Time (years) Assuming steady-state flow across a 1m thick fault zone
• How long for across-fault leakage to cause a 100m rise in FWL?
Pressure potential difference (bars)
Permeability is a seal property relevant to “exploration” as well as production timescales
Fault permeability algorithms
x
y
z Fault zone
3) RECENT CASE APPLICATIONS
Well 1 Well 2 ∆OVP = 70bar
Q
Q A
1. North Sea case: aquifer pressure prediction
∆OVP1 = Xbar, L1 = xkm
Well-1 Well-2
Well-4 ∆OVP3 = Ybar, L3 = ykm
Prospect
2. CIS case: dynamic charge rates
APPLICATION 1: PROSPECT PRESSURE SCENARIOS
Range of Prospect A
U. Jurassic unconformity
Base chalk
Pressure potential (m)
Dep
th
Crest depth uncertainty
Well 2 aquifer
Well 1 aquifer
Approximate 1D calculation:
3m 1000m 100m
∆P1 ∆P2
∆PTOT = 70bar
Q Q Q Q
x
Prospect A
∆P1 = 0.02 bars ∆P2 = 69.98 bars
Results
Well 1
Q = k * A ∆P
µ ∆x
Well 2 ∆OVP = 70bar
Q
Q A
APPLICATION 2: DYNAMIC FILLING ESTIMATIONS
∆OVP1 = 14bar, L1 = 10km
Well 1 Well 2
NE
Flow restriction across low-permeability fault
What fault permeability required to support a given ∆OVPf ?
Wat
er h
ead
? OVP ~ 200b OVP ~ 190b
Well 4 (OVP 40 – 70b)
Q Q
Q
If: 10 m wide fault zone : kfault = 0.32 µD
1 m wide fault zone : kfault = 32 nD
Hydrodynamic gradient : 14m/kmGWC tilt : 22m/km (with TAF=1.53)
Azimuth: N10°W
BC i 4 P ti l f lt bilit K 0 005
Hydrodynamic gradient : 14m/kmGWC tilt : 22m/km (with TAF=1.53)
Azimuth: N10°W
BC i 4 P ti l f lt bilit K 0 005
2D water potential model (internal study 2011)
∆Pf 130 bars
Approximate 1D model:
A
10km 10m or 1m
∆P1 = 14bar ∆Pf
x k1 = 3mD
kf ?
If Q constant : Q = k1 * A * ∆P1 µ x1
kf * A * ∆Pf µ xf
=
IS THE FAULT PERMEABILITY ESTIMATE REASONABLE?
Fault permeability estimate is compatible with prediction from algorithm
10 m wide fault zone
1 m wide fault zone
0.32µD
32nD
nD range
mD range
FWL
PRESSURE SYNTHESIS
80 - 100 bars across-fault difference in gas legs
Max ~135 bars across-fault difference in water legs
Min ~110 bars across-fault difference in water legs
S crest against fault
Well 3 Well 2
N S
Main fault
Crests against fault
∆GWC
Static pressure potential
Nor
th c
ompt
Sout
h co
mptGas gradient
Potential (m)
Dep
th (m
ss)
Nor
th c
ompt
Sout
h co
mptGas gradient
Potential (m)
Dep
th (m
ss)
Sout
h co
mptGas gradient
Potential (m)
Dep
th (m
ss)
Gas leg in static equilibrium
∆OVP(fault)
N crest against fault
Down-dip spill to N
Down-dip spill to N
+100m uncertainty in spill depth
Pressure potential
(Grosjean et al., 2008)
Pre-drill view Post-drill view
16 -
DYNAMIC TRAPPING: FAULT COMMUNICATION BEHAVIOUR
Well 2
Appr
ox.
scal
e
xx00
xx00
xx00
xx00
xx00 m
Relay tip-controlled fault spill
Across-fault hydrodynamic leakage
Up-fault hydrodynamic filling
Well 3
Strong hydrodynamics: • No classic “fault sealing” methodology applicable • but pre-drill fault permeability prediction conforms to pressure compartmentalisation
Charge from basin Up-fault
charge
Strong hydrodynamic gradient
Seismic amplitude anomalies indicate possible filling down to
spill depth.
Quaternary fill-to-spill through fault is reasonable: across-fault -> 21TCF/Myr, up-fault 1 – 10 TCF/Myr
17 -
CONCLUSIONS
● Case studies of hydrodynamics allow us to advance concepts;
● Fault permeability is an important seal property in exploration as
well as production issues;
● Recently-developped fault permeability algorithms have been
implemented into new workflows where OVP / hydrodynamics is
important.
● Applications to pressure/seal evaluation include aquifer PPP and
dynamic charge/leak rates for prospect in-place volume risking
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