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Xiaochen Wei, Qi Li, Xiaying Li, Zhiyong Niu, Xiangjun Liu, Lixi Liang, "Effects of Different Penetration Patterns on a Fault during Underground Fluid Injection", Geofluids, vol. 2019, Article ID 2027510, 15 pages, 2019. https://doi.org/10.1155/2019/2027510
Effects of Different Penetration Patterns on a Fault during Underground Fluid Injection
At underground fluid injection sites with natural faults, understanding how to avoid the subsequent fault reactivation and induced seismicity plays a crucial role in the success of subsurface anthropogenic activities. In this work, with the objective of avoiding risky faults in site selection in the Shengli Oilfield, we investigated the faults that are usually encountered in the target demonstration zone; based on the geophysical observations of fault structures, we designed different fault tectonic scenarios to investigate the different penetration patterns of faults. We used the finite element-based numerical method to assess the influence of the effective lateral and vertical reservoir transmissivity in each fault penetration pattern. Our results indicate that when a permeable fault intersects into the target reservoir, it presents both barrier effect to reservoir transmissivity within the target reservoir and hydraulic connection between reservoirs. The effective lateral reservoir transmissivity is dominated by the barrier effect of the fault, and the effective vertical reservoir transmissivity is dominated by the hydraulic connection between reservoirs. Relatively impermeable faults with less contact with the target aquifer make higher effective lateral reservoir transmissivity and lower effective vertical reservoir transmissivity, which would mitigate the risk of caprock failure and the magnitude of the induced seismicity.
Over the last four decades, the induced seismicity has been observed to result from a certain number of underground fluid injection activities including hydrothermal- and petrothermal-enhanced geothermal systems , water subsurface disposal , enhanced oil/gas recovery (EOR/EGR) , and carbon capture and storage that enable the capture of CO2 from industrial processes and storage in depleted oil/gas fields or deep saline formations . A successful commercial scale deployment of underground fluid injection requires assurance that the injected fluid at each potential geological sequestration site is confined [5–8]. The most significant aspect of containment is the seal potential of the reservoir , which could be defined as the seal geometry and seal integrity [10–12]. Seal geometry refers to the thickness and lateral extent of the caprock, as well as fault tectonics. For long-term security of fluid injection in geological reservoir, the caprock must have sufficient lateral extent to cover the reservoir [13, 14]. Faults are complex and heterogeneous geological systems, and reservoir-scale faults in low-permeability deformed reservoir target for underground fluid injection can present highly complex architecture, which might influence the hydromechanical behavior of the fault system [15–17]. Seal integrity refers to the geomechanical properties of the geological sequestration site. These properties are controlled by the mineralogy , the regional and local stress fields , and stress changes induced by underground fluid injection . The perturbation of the stress field within a geological formation during and after fluid injection may lead to mechanical failures of the caprock and interior faults . Natural faults are inevitable at CO2-EGS sites such as the North-German Basin and Taupo Volcanic Zone in New Zealand [22, 23]. Underground fluid injection reduces the effective normal stress and brings a preexisting fault to failure, which could generate seismicity occasionally large enough to cause damage [24–26]. Another possible risk related to failure is the potential creation of new leakage pathways for the trapped fluid that may eventually induce earthquakes felt at the ground surface [27–30]. Fundamentally, a well-characterized site must shed light on at least two features of the subsurface: the caprock confining the reservoirs and any faults or fractures crosscutting the formation [31–34]. When caprock is crosscut by faults, its vertical sealing potential will be affected in certain degrees . This critical situation is well illustrated by what happened at some actual sequestration sites (e.g., Weyburn, Canada) . An important question is then related to the issue of faults crosscutting the caprock and the reservoir, i.e., different spatial distributions of a fixed-length fault, which might influence the stress distribution and eventually influence the fault stability during fluid injection [37, 38].
Previous studies on the fault tectonics have indicated the importance of the fault zone architecture to the seal integrity [39–41] and the fault behavior [42–44]. Concerns have been raised related to the complex tectonics in the reservoirs and the surrounding faults, as well as the physical and chemical processes impacting fluid migrations and containment under field conditions [45–47]. The potential for geomechanical failure caused by underground fluid injection has been investigated [15, 16, 48, 49]. Regarding the issue of fault architecture, the first investigations revealed that the spatial distribution of the fault might influence the stress distribution and eventually the fault stability during fluid injection [50–53]. An evolution of the damage zone’s properties with distance from the fault core has been assumed by Rohmer et al. , and a geostatistical approach based on observations of fault structures at Navacelles (France) was used to investigate fault stability during injection . Zoback and Gorelick  claimed that carbon geological sequestration in deep saline formations is very likely to trigger induced seismicity capable of damaging the caprock, which could ruin the objective of keeping fluid stored deep underground. However, Vilarrasa and Carrera  recently argued that induced earthquakes that are large enough to be felt due to geologic carbon geological sequestration are unlikely because sedimentary formations, which are softer than the crystalline basement, are rarely critically stressed. In addition, they argue that fluid leakage through fault reactivation is unlikely because the high clay content of caprock ensures a reduced permeability and increased entry pressure along localized deformation zones. In fact, their standpoints are under the assumption of specific reservoir-caprock sequences and seal geometry, as well as their geomechanical properties and injected fluid behavior under long-term geological sequestration. Thus, it is necessary to have a sufficient knowledge about the tectonics and mechanical properties of formations in the operation site of fluid injection, as well as their long-term influence to ensure that injected fluid would be stored safely over the intended life of the injection project [55, 56].
In this work, with the objective of assessing earthquake risk in the operating region, we investigated the fault slippage with different penetration patterns that are usually encountered in the G89 Block of the CO2-EOR demonstration zone in the Shengli Oilfield (Shandong province, China) . The relatively lower permeability than that of the reservoir of the fault has a significant impact on the pressure perturbations within the thick reservoir. When the fault penetrates into different reservoirs, it acts in both the barrier within the target reservoir and hydraulic connection between reservoirs. Focusing on the effective lateral reservoir transmissivity and effective vertical reservoir transmissivity under three penetration patterns caused by different fault tectonic scenarios, we introduce numerical model-coupled changes of pore pressure and stresses. In Section 2, the geomechanical models are described in detail for different scenarios of a fault penetrating into regional caprock, as well as their geomechanical properties. In Section 3, the influence of effective lateral reservoir transmissivity is thoroughly evaluated on pore pressure change, vertical displacement, and the fault slippage and a sensitivity analysis of hydraulic connection is carried out. Finally, the main findings and conclusions are summarized in Section 4.
2. Model and Methodology
2.1. Theoretical Background
2.1.1. Frictional Slip on Fault
An extended version of the classical isotropic Coulomb friction model is provided with all contact analysis capabilities. The extensions include an additional limit on the allowable shear stress and isotropic friction coefficient.
The standard Coulomb friction model assumes that no relative motion occurs if the equivalent frictional stress is less than the critical stress , which is proportional to the contact pressure , in the form , where is the friction coefficient that can be defined as a function of the contact pressure , the slip rate , the average surface temperature at the contact point, and the average field variables at the contact point.
Here, it is possible to put an additional limit on the critical stress: ; if the equivalent stress is at the critical stress , slip can occur. If the friction is isotropic, the direction of the slip and the frictional stress coincide, which is expressed in the form where is the slip rate in direction and is the magnitude of the slip velocity.
According to the relationship presented by Hanks , the quantification of the overall size of an earthquake is generally based on the seismic moment () which is defined by , and we can approach the seismic moment from the average fault slippage over the ruptured area and the rock shear modulus . In terms of seismic moment, the magnitude of an earthquake is given by . Therefore, to some extent, in this study, the average fault slippage determines the magnitude of the seismic event induced by the simulated fluid injection.
2.1.2. The Master-Slave Contact Algorithm
Herein, a master-slave contact algorithm is adopted for governing the interaction behavior between a fault and the surrounding rock. Figure 1 illustrates a typical master-slave slide line segment. Before initiating the search for the nodal subset of the master surface nodes that will interact with each node on the slave surface, the unit normal vectors are computed for all of the nodes on the master surface. Additional unit normal vectors are computed for each segment at a distance from the end of each segment, where is a fraction and is the length of the segment.
For the two-dimensional small-sliding deformable contact, a point on the contact line associated with a slave node is represented by the vector:
As described previously, the line’s anchor point and its tangent vector are functions of the current master node coordinate. Hence, the vector is, in general, a nonunit vector. Linearization of equation (3) yields where , , and . Taking the dot product of equation (4) with results in the following expression for :
Likewise, taking the dot product of equation (4) with the normalized tangent vector and setting results in the following expression for the variation in slip:
2.2. Conceptual Model
To investigate the stress changes and fault responses during CO2 storage, we used a geomechanical model that coupled changes of pore pressure and stresses. The numerical models present typical penetration patterns on faults that are usually encountered in the G89 Block of the target demonstration zone in the Shengli Oilfield at an approximate depth of 1000 m . The target zone is located in the south-west of the Shengli Oilfield, which was estimated to have approximately 40 million tons of initial oil-in-place. The G89 Block is in the middle of the Jinjia-Zhenglizhuang-Fanjia structure, which belongs to the Dongying depression. It covers an area of 4.1 km2 and is composed of several interbedded producing zones (Figure 2) . The target reservoir is filled with fine quartz sandstone, and fluid injection was proposed for secondary recovery.
2.3. Model Setup
In this study, to reflect the real regional structural settings in the demonstration zone, based on their geophysical observations of fault structures in the G89 Block in Figure 2, three typical penetration patterns on a fault are currently considered (Figure 3). 2-D numerical models are employed to take into account the geomechanical aspects of supercritical CO2 injection into the reservoir. To restrict the complexity of our model conceptualization and better identify the individual unit behavior, two assumptions were made: (1) two reservoir-seal associations are used while the lower reservoir is the targeted reservoir. Instead of an aquifer system with numerous complex interbed distribution reality, two reservoir-seal associations allow us to understand such a formation’s behavior in a straightforward manner and (2) the hydraulic connection of each fault zone is assumed isotropic. As the constant permeability in the fault zone is considerably lower than that in the aquifer, it is only a trivial extension to include anisotropic permeability . The injected supercritical CO2 is defined with a density of 1.1 g/cm3 and viscosity of 0.02 mPa·s, and the phase change is neglected in this work.
Scenario 1. The fault does not penetrate into the upper reservoir. The lower caprock is above the target reservoir, and the rocks in the lower caprock have not been completely penetrated. There are still intact sections with a certain thickness on the top, and the fault retains a vertical sealing ability. The fluid cannot leak out through such a fault. This pattern is the most developed scenario in the demonstration zone, accounting for 66% of the total number of faults.
Scenario 2. The permeable fault penetrates into the upper reservoir but does not reach the upper caprock. In this way, the transverse sealing ability is still strong. The hydraulic connection of the fault under such a scenario is good enough to allow the leakage of fluid through the fault and diffusion from the target reservoir to the upper reservoir. The Scenario 2 fault in the demonstration zone is relatively developed, accounting for 30% of the total number of faults.
Scenario 3. The permeable fault penetrates the two reservoirs into the upper caprock. Due to the hydraulic connection of the fault, the fluid could theoretically leak into the upper reservoir along the fault .
Figure 4 shows the geometry and initial conditions of the numerical model () that we used for modeling the three types of fault settings. The model extends from 1000 to 2500 m in depth and horizontally far enough from the injection zone (10000 m) to simulate laterally infinite conditions. The fault zone is located at a distance of 800 m from the injection well, dipping 60°, with a 50 m length along the dip and a 700 m long fault surface. The reservoir is initially saturated by water and the initial pore pressure is assumed to be hydrostatic (shown as in Figure 4). For each of the tectonic stress regimes, the vertical stress is considered to be given by the weight of the overburden and vertical stress from the weight of overburden rock for a density of kg/m3, with horizontal stress being scaled by a factor 0.6 of the vertical stress, i.e., . The fluid is injected into the target reservoir at -2000 m for 20 years through a horizontal well, and the injection pressure is stable at 30 MPa, which corresponds to the industrial injection pressure. The rock mechanical properties are based on available logs and well data from the field and laboratory experiments. Hydraulic and mechanical properties for the different layers (the caprock, reservoir, and fault) are listed in Table 1 (after [53, 62]), and the target reservoir was fractured before CO2-EOR operation.
The schematic views of the model geometry and the corresponding numerical models, as well as the boundary conditions, are presented in Figure 4. The lengths of the faults in each scenario are the same; the only difference is the intersection of fault into formations. The multiple layers and the fault are modeled using an elastoplastic isotropic Mohr-Coulomb model. The normal displacements applied to the lateral boundaries were fixed to zero. The vertical displacement at the bottom of the geomechanical model was also fixed to zero. A calculated initialization was performed to reach a geomechanical equilibrium between the initial geostress fields and the applied boundary conditions of the model. To enhance the computational accuracy and efficiency, a structured mesh with 26902 elements was adopted in the numerical model. The grid around the injection point and faults was densified, and the size of the finest element is .
The pore pressure distribution was presented in Figure 5 after 20 years of injection. In Scenario 1, the fault intersects the target reservoir on a very large surface and so creates a low-permeability barrier in the upper portion of the reservoir, while in Scenario 3, the fault intersects the target reservoir on a relatively smaller surface and Scenario 2 is an intermediate case. In Scenario 2 and Scenario 3, the permeable fault penetrates into the upper reservoir, the injected fluid leaks along the fault and results in a pore pressure rise in the upper reservoir.
3. Results and Discussion
3.1. Pore Pressure Changes
An increase in the pore pressure results in a general reduction of the mean effective stresses in the reservoir and caprock system. According to the work of Mathias et al. , the lithostatic stress varies vertically from the free ground surface and the largest change is occurring in the lower part of the caprock. For this reason, in this study, we focus on the mechanical responses along the interface between the lower caprock and target reservoir from the injection well to the fault at different times and locations after the start of injection.
Figure 6 presents the pore pressure changes along the interface (shown in insert sketch plots) at different times. As shown, pore pressure changes increase with time at all locations after the injection starts, and at specific times, the maximum increase in pore pressure occurs near the injection well zone and farther locations experience less pore pressure increase. After 20 years of injection, the pore pressure at the crosscutting point of the fault point increases to 17.853 MPa, 17.851 MPa, and 17.755 MPa in Scenario 1, Scenario 2, and Scenario 3, respectively. The relatively lower pore pressure at point in Scenario 3 indicates the barrier effect of the fault within the target reservoir, which depends on the section of the reservoir thickness that is intersected by the fault. When a fault with relatively lower permeability intersects into the targeted reservoir in a large section such as those in Scenario 1 and Scenario 2, the effective lateral reservoir transmissivity is significantly reduced and the injected fluid accumulates at the fault and generates significant overpressure, while in Scenario 3, the much less contact between the fault and the target reservoir indicates better effective lateral reservoir transmissivity and, consequently, pore pressure would experience less increase.
Other than the barrier effect of the fault within the target reservoir, the hydraulic connection between reservoirs enables the injected fluid to flow upward into the upper reservoir and thus dissipates the overpressure at the fault. As shown in Figure 4, the pore pressure transmits from the target reservoir to the upper reservoir along the fault in Scenario 2 while hydraulic connection is missing in Scenario 1 for the fault does not reach the upper reservoir. For this reason, the relatively lower pore pressure at point in Scenario 2 than in Scenario 1 suggests that the hydraulic connection between reservoirs in Scenario 2 mitigate the overpressure at the fault, even in a limited scale.
Figure 7 illustrates the variations of pore pressure versus time at three different locations with horizontal distances (200 m, 400 m, and 600 m) along the interface between the caprock and the reservoir from the injection well for the three scenarios. As shown, for the locations away from the injection well such as P2 and P3, the pore pressure does not show significant increase after the start of fluid injection in a short time, but after a period of fluid injection, a large volume of the injected fluid leads to an overpressure at all locations in the reservoir and the pore pressure rises towards the initial injection pressure in all scenarios. Pore pressure increases gradually from the hydrostatic pressure 17.50 MPa with time at all three locations. This result is consistent with the work of many different researchers on actual geological sequestration sites [17, 56].
The dashed lines in Figure 7 indicate the time when the pore pressure starts to increase at P1, P2, and P3 in the three scenarios. As shown, the time for the pore pressure to start to rise is dependent on the effective lateral transmissivity of the reservoir. The higher effective lateral transmissivity of the reservoir in Scenario 3 significantly brings forward the time for pore pressure to start to rise than in other scenarios. And at P2 and P3, due to the relatively better effective lateral transmissivity in Scenario 2, the time for pore pressure to start to rise is several days earlier than that in Scenario 1. It can thus be concluded that a higher effective lateral transmissivity of the reservoir brings forward the time for pore pressure to start to rise.
Figure 8 shows that the vertical displacement increases gradually with time during the fluid injection in all three scenarios. Due to the high overpressure near the injection well, the effective stresses change accordingly and thus generate greater vertical displacements near the injection well. As shown, the maximum increase in vertical displacement occurs around the injection well and farther locations experience less of an increase . This result highlights that the higher effective lateral reservoir transmissivity leads to relatively smaller overpressure, which leads to the corresponding smaller scale of vertical displacement.
3.2. Failure of Caprock
Caprock failure during underground fluid injection and the corresponding induced seismicity has been studied previously by many different researchers from the perspective of the stress state [64–66]. A higher pore pressure rise corresponds to a higher reduction in effective stress; risk of failure rises with time before fluid dissolution . Figure 9 presents the stress state at point at the caprock interface near the injection well. As shown, the vertical effective stress decreases with time shortly after the injection starts. After 20 years, the effective stress changes () are 4.476 MPa, 4.472 MPa, and 4.469 MPa in Scenario 1, Scenario 2, and Scenario 3, respectively. In an ideal normal fault stress regime where and , overpressure can potentially increase the horizontal stresses , while the vertical stress is likely to remain unaffected, so the diameter of the Mohr circle is reduced as a result of overpressure. Because of the 9 MPa cohesion, the caprock undergoes no failure and remains stable in all three scenarios after 20 years of fluid injection. Due to the higher effective stress changes in Scenario 1, it is more critical compared with those in other scenarios.
3.3. Fault Slippage
Despite the tiny differences in pressure and displacement between the three scenarios, the slippage is very different. Figure 10 shows the fault slippage lengths and pore pressure distributions along the fault surfaces in the three different scenarios. After fluid injection, the original hydrostatic pore pressure distributions show clear variation at the interface of the caprock and the reservoir. Because of the different values of friction angle in the caprock and the fault, the most stressed region in the caprock near the injection well does not fail while the fault fails.
The maximum slippage length value and its location are different in each scenario. In Scenario 1 and Scenario 2, the induced fault slippages reach the maximum values in the target reservoir and decrease with distance into the caprock and present significant change at the interface between the lower caprock and the target reservoir. The reason behind this behavior is in the different material properties, the faults present larger slipping length in the high-permeability reservoir than in the caprock, this tendency is more significant in Scenario 3, the two peak fault slippage values are located in the target reservoir and the upper reservoir, and this result is in consistency with the research of Cappa and Rutqvist .
As discussed above, the effective lateral reservoir transmissivity, which controls the overpressure at the fault, is significantly affected by the barrier effect of the fault. The effective vertical reservoir transmissivity is controlled by hydraulic connection between reservoirs; the average fault slippages in Scenario 2 (2.735 mm) and Scenario 3 (2.022 mm) are greater than in Scenario 1 (1.944 mm) and so does the maximum fault slippage. The magnitude of fault slippage is affected by both the effective lateral reservoir transmissivity and the effective vertical reservoir transmissivity. The effective vertical reservoir transmissivity dominates the magnitude of fault slippage; when hydraulic connection is missing in Scenario 1, the induced fault slippage remains low; on the other hand, lower effective lateral reservoir transmissivity could generate significant overpressure along the fault; for this reason, the level of fault slippage in Scenario 2 is greater than that in Scenario 3.
Moreover, the activation of a similar shear slip within the caprock or within the reservoir has very different effects. Even though the faults present larger slipping length in the reservoir than in the caprock, the higher shear modulus in the caprock would also enlarge the seismic moment. From these simulation results and the relationships presented in Section 2.1.2, we can calculate the magnitude of an earthquake from and . With an assumed lateral extent of 1 km for rupture since our simulations are conducted in a plane strain model, the magnitudes of 1.58, 1.53, and 1.24 are estimated for the seismic events induced by the simulated fluid injection in Scenario 1, Scenario 2, and Scenario 3, respectively.
3.4. Sensitivity Analysis of Hydraulic Connection
In the previous section, the presented fault slippage is found to be largely dependent on the effective vertical reservoir transmissivity, which is determined by the hydraulic connection between reservoirs. In this section, we present a sensitivity analysis to clarify the influence of hydraulic connection on the simulation results.
Figure 11 shows that the reduced effective vertical reservoir transmissivity enhances the overpressure along the fault surface within the target reservoir. When the fault permeability decreases to mD, the corresponding average fault slippage is 2.622 mm. In contrast, the enlarged fault permeability mD enhances the vertical reservoir transmissivity accordingly; as a consequence, the pore pressure shows no obvious change but the corresponding average fault slippage reaches maximum in this sensitivity study at 2.764 mm. This result highlights that both the average fault slippage and maximum fault slippage are dominated by the effective vertical reservoir transmissivity; when a fault connects two reservoirs, a higher fault permeability would enlarge the fault slippage and the magnitude of the corresponding induced seismicity.
With the objective of avoiding risky faults in site selection in the Shengli Oilfield, we investigated the faults that are usually encountered in the target demonstration zone. Based on their geophysical observations of fault structures, we designed different fault tectonic scenarios to investigate the different penetration patterns of faults. We implemented a coupled flow and stress model to investigate the influence of the effective lateral and vertical reservoir transmissivity in three different scenarios. We thereby reached the following conclusions: (1)When a permeable fault intersects into the target reservoir, to reservoir transmissivity, it presents both barrier effect within the target reservoir and hydraulic connection between reservoirs. The effective lateral reservoir transmissivity is dominated by the barrier effect of the fault, which depends on the section of the aquifer thickness that is intersected by the fault. The effective vertical reservoir transmissivity is dominated by the hydraulic connection between reservoirs, while the hydraulic connection enhances the effective lateral reservoir transmissivity only in a limited scale(2)A higher effective lateral reservoir transmissivity could effectively reduce the overpressure in the aquifer and the corresponding scale of vertical displacement, as well as bring forward the time for pore pressure to start to rise at the locations away from the injection well(3)Although the caprock undergoes no failure and remains stable in all three scenarios after 20 years of fluid injection, risk of failure rises with time and the most critical state occurs at the end of injection. Compared with those in Scenario 2 and Scenario 3, the situation in Scenario 1 is more critical for higher effective stress change caused by lower effective lateral reservoir transmissivity(4)The induced fault slippage reaches the maximum value in the target reservoir and decreases with distance into the caprock. The effective vertical reservoir transmissivity dominates the magnitude of fault slippage, and better hydraulic connection between reservoirs could enlarge the fault slippage and the magnitude of the corresponding induced seismicity
Finally, in underground fluid injection operation such as hydrothermal- and petrothermal-enhanced geothermal systems with hidden faults in the target zone, relatively impermeable faults with less contact with the target aquifer make higher effective lateral reservoir transmissivity and lower effective vertical reservoir transmissivity. Based on the above conclusions, this fault penetration pattern with less contact to the target aquifer would mitigate the risk of caprock failure and the magnitude of the induced seismicity.
The experiment data used to support the findings of this study are available from the corresponding author upon request.
Conflicts of Interest
The authors declare that they have no conflicts of interest.
This work was mainly supported by the National Natural Science Foundation of China (NSFC) under Grant no. 41872210, the Open Research Fund of the State Key Laboratory of Geomechanics and Geotechnical Engineering under Grant no. Z017008, and the Young Scholars Development Fund of SWPU under Grant no. 201699010097. We would also like to thank the financial support provided by the China National Key Technology R&D Program (Grant no. 2012BAC24B05), the United Fund Project of the National Natural Science Foundation of China (Grant no. U1262209), and the National Science and Technology Major Project of the Ministry of Science and Technology of China “Development of Large Oil and Gas Field and Coalbed Methane” (Grant no. 2016ZX05044-004-001).
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