CN114923945B - Tailing filling body pore water pressure simulation method in high-temperature stope and application thereof - Google Patents
Tailing filling body pore water pressure simulation method in high-temperature stope and application thereof Download PDFInfo
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Abstract
The invention discloses a method for simulating pore water pressure of a tailing filling body in a high Wen Caichang area and application thereof, comprising the following steps: based on a pore thermoelastic theory framework, a non-isothermal pore water pressure evolution model of the filler is established, pore water pressure evolution rules of filler units with different initial temperatures under the action of temperature load are analyzed, and then a filler behavior response mechanism under complex geothermal environment conditions is clarified, so that theoretical support is provided for providing a targeted filling optimization scheme and realizing safe and clean exploitation of deep resources.
Description
Technical Field
The invention relates to the technical field of mineral resource development, in particular to a method for simulating pore water pressure of a tailing filling body in high Wen Caichang and application thereof.
Background
Mineral resource development is an important way to provide material resources for society, however, conventional mining processes will produce large amounts of subsurface goaf and surface pile-up of tailings, which in turn pose serious hazards to mine safety production and natural ecological environment (Benzaazoua et al, 2004;Kesimal et al, 2005; bussire, 200 7; xu Wenbin, 2015; wu Aixiang, 2016). Under the push of ever-increasing safety production standards and environmental protection pressures, the underground disposal of tailings is becoming an important way to achieve green clean mining of mineral resources (N asir and Fall,2009;Ghirian and Fall,2013a; wu Aixiang, et al, 2018). By mixing the tailings, cementing agent, and water in a certain ratio and backfilling the tailings to the underground goaf, the tailings filling technique not only avoids a great deal of exposed accumulation of the tailings on the ground surface, but also can significantly improve the surrounding rock stability of the underground stope, and can allow no ore pillar to remain and further improve the ore recovery rate (Kesimal et al 2005;Klein and Simon,2006;Wi tteman and Simms,2017;Lu et al, 2020 a).
Although tailings filling technology continues to bring tremendous environmental and economic benefits to underground resource exploitation, recent field monitoring work has found many times that the filling body has abnormal behavior in deep mines, mainly as the pore water pressure and the earth pressure can still generate a sharp increase under the condition of filling suspension (Thompson et al, 2011,2012,2014;Hasan et al, 2014). Because the acting force of the bottom retaining wall in the filling process determines the stability of the filling system, the pressure abnormality phenomenon discovered by on-site monitoring can possibly cause the damage of the filling retaining wall so as to seriously threaten the safety of underground personnel and the mine production efficiency. However, the current research work has not yet established perfect understanding of the filler behavior response law under deep complex temperature environmental conditions. The surrounding rock temperature of the stope continuously rises along with the increasing resource exploitation depth under the action of the ground temperature gradient (Fall et al, 2010; bell et al, 2018;Wang et al,2019; how full tide is, etc., 2005; thank and equal, 2015; goldson, etc., 2003), so that the multi-field coupling response research of the filling body under the complex temperature environment condition is developed, and the action mechanism of the filling body in the high-temperature stope is revealed, and the method has important theoretical and engineering significance for realizing the safe and clean development and utilization of deep resources.
In the prior art, a filler temperature-seepage-mechanics-chemical field coupling model is established by considering the energy generation and migration process, and can be used for predicting the evolution rules of the filler temperature, the water pressure, the soil pressure and the like (Cui and Fall, 2015,2016,2017,2018).
The thermal expansion effect of water is not considered in the prior art: the cement hydration exotherm process consumes free water, which in turn causes hydraulic dissipation. However, since the coefficient of thermal expansion of water is generally greater than that of solid particles, the rise in temperature caused by the exothermic heat of hydration of the cement will cause an increase in the pore water pressure of the pack. While hydrothermal boost has been demonstrated by in situ testing of Thompso et al (2012). This study found that even if the filling process was terminated, the filled body could have an abnormal rise in water pressure due to an increase in temperature caused by the exothermic heat of hydration of the cement. In the prior art, the thermal expansion effect of water is ignored, so that the water pressure abnormality caused by thermal expansion deformation cannot be described.
In the second prior art, a filling body seepage-mechanical-chemical field coupling model is established by considering free water consumption and physical and mechanical property evolution caused by hydration reaction, and can be used for predicting evolution rules of filling body water pressure, soil pressure and the like (Helinski et al, 2007,2011;Muir Wood et al, 2016; lu, 2017).
The influence of temperature is not considered in the second prior art: the cement hydration exothermic process not only accelerates the chemical reaction rate and increases the strength of the filler, but also causes water evaporation, thereby reducing pore water pressure. Meanwhile, the change of temperature also causes the change of the viscosity coefficient of the fluid, thereby affecting the evolution rule of the seepage field. In addition, as the mining activity depth is increased, the ambient temperature of the stope is increased under the action of the ground temperature gradient, so that the influence of the temperature on the behavior characteristics of the deep filling body is more remarkable. In the second prior art, the effect of temperature on the filling body is ignored, so that the behavior characteristics of the filling body in the complex occurrence environment cannot be accurately described.
Reference to the literature
Benzaazoua,M.,Marion,O.,Picquet,I.,Bussiere,B.2004.The use of pas tefill as a solidification and stabilization process for the control of acid mine dr ainage.Miner.Eng.17,233–243；
Kesimal,A.,Yilmaz,E.,Ercikdi,B.,Alp,I.,Deveci,H.2005.Effect of pr operties of tailings and binder on the short–and long–term strength and stability of cemented paste backfill.Materials Letters 59(28),3703–3709；
Bussière,B.2007.Colloquium 2004:Hydrogeotechnical properties of hard r ock tailings from metal mines and emerging geoenvironmental disposal approach es.Can.Geotech.J.44,1019–1052；
Xu Wenbin, song Weidong, cao Shuai, jiang Guojian, wu Feng, & Jiang Lei (2015) underground mine stope group stability analysis and control techniques, journal of mining and safety engineering, 32 (04), 658-664;
wu Aixiang, wang Yong, & Wang Hongjiang (2016) paste filling technology and trend metal mines, 07, 1-9;
Nasir,O.,and Fall,M.(2009).“Modeling the heat development in hydratin g CPB structures.”Computers and Geotechnics,36(7),1207–1218；
Ghirian,A.,Fall,M.2013.Coupled thermo–hydro–mechanical–chemical beh aviour of cemented paste backfill in column experiments.Part I,Physical,hydra ulic and thermal processes and characteristics.Engineering Geology 164,195–20 7；
Klein,K.,Simon,D.2006.Effect of specimen composition on the strength development in cemented paste backfill.Canadian Geotechnical Journal 43,310 –324；
Witteman,M.L.,Simms,P.H.2017.Unsaturated flow in hydrating porous m edia with application to cemented mine backfill.Canadian Geotechnical Journal 54,835–845；
Lu,G.D.,Yang,X.G.,Qi,S.C.,Fan,G.,Zhou,J.W.,2020a.Coupled chem o-hydro-mechanical effects in one-dimensional accretion of cemented mine fills. Eng.Geol.267,105495；
Thompson,B.D.,Bawden,W.F.,and Grabinsky,M.W.2011.In-situ monitori ng of cemented paste backfill pressure to increase backfilling efficiency.Canadia n Institute of Mining Journal,2(4):1–10；
Thompson,B.D.,Bawden,W.F.,and Grabinsky,M.W.(2012).“In situ measurements of cemented paste backfill at the Cayeli mine.”Canadian Geotech nical Journal,49(7),755–772；
Thompson,B.D.,Simon,D.,Grabinsky,M.W.,Counter,D.B.,Bawden,W.F. 2014.Constrained thermal expansion as a causal mechanism for in situ pressur e in cemented paste and hydraulic backfilled stopes.Proceedings of the 11th Int ernational Symposium on Mining with Backfill,Perth,365–378；
Hasan,A.,Suazo,G.,Doherty,J.,Fourie,A.2014.In situ measurements o f cemented paste backfilling in an operating stope at Lanfranchi Mine.Proceedi ngs of the 11th International Symposium on Mining with Backfill,Perth,327–3 36；
Fall,M.,Célestin,J.C.,Pokharel,M.,Touré,M.2010.A contribution to un derstanding the effects of curing temperature on the mechanical properties of mi ne cemented tailings backfill.Engineering Geology114,397–413；
Belle,B.,Biffi,M.,2018.Cooling pathways for deep Australian longwall c oal mines of the future.Int.J.Min.Sci.Technol.28,865–875；
Wang,M.,Liu,L.,Zhang,X.Y.,Chen,L.,Wang,S.Q.,&Jia,Y.H.(20 19).Experimental and numerical investigations of heat transfer and phase change characteristics of cemented paste backfill with PCM.Applied Thermal Engineer ing,150,121–131；
how full the tide is, xie Heping, peng Suping, jiang Yaodong.2005. Deep mining rock mass mechanics research. Report on rock mechanics and engineering, 24 (16), 2083-2813;
xie Heping, peak Ju Yang.2015. Deep rock mechanics research and exploration. Rock mechanics and engineering journal 34 (11), 2161-2178;
goldson, & Li Xibing, (2003) the current state of non-ferrous deep well mining research and scientific frontier, mining research and development, S1,1-5;
Cui,L.,Fall,M.2015.A coupled thermo-hydro-mechanical-chemical model for underground cemented tailings backfill.Tunn.Undergr.Sp.Tech.50,396–4 14；
Cui,L.,Fall,M.2016.Multiphysics model for consolidation behavior of ce mented paste backfill.ACSE Int.J.Geomech.17(3):23p；04016077-23；
Cui,L.,Fall,M.2017.Modeling of pressure on retaining structures for un derground fill mass.Tunn.Undergr.Sp.Tech.69,94–107；
Cui,L.,Fall,M.2018.Modeling of self-esiccation in a cemented backfill s tructure.Int.J.Numer.Anal.Methods Geomech.42:558–583；
Thompson,B.,Bawden,W.,Grabinsky,M.2012.In situ measurements of ce mented paste backfill at the Cayeli mine.Canadian Geotechnical Journal 49,755 –772；
Helinski,M.,Fourie,A.,Fahey,M.,Ismail,M.2007a.Assessment of the s elf-desiccation process in cemented mine backfills.Can.Geotech.J.44,1148–11 56；
Helinski,M.,Fahey,M.,Fourie,A.2011.Behavior of cemented paste back fill in two mine stopes:measurements and modeling.J.Geotech.Geoenviron.E ng.137,171–182；
Muir Wood,D.,Doherty,J.P.,Walske,M.L.2016.Deposition and self-weig ht consolidation of a shrinking fill.Géotechnique Lett.6,72–76；
Lu,G.2017.A model for one-dimensional deposition and consolidation of shrinking mine fills.Géotechnique Letters.7:347-351；
Wu,D.,Fall,M.,Cai,S.2014.Numerical modelling of thermally and hydr aulically coupled processes in hydrating cemented tailings backfill columns.Inter national Journal of Mining,Reclamation and Environment,28(3),173–199；
Fahey,M.,Helinski,M.,Fourie,A.2009.Some aspects of the mechanics o f arching in backfilled stopes.Canadian Geotechnical Journal 46,1322–1336；
Fahey,M.,Helinski,M.Fourie,A.2010.Consolidation in accreting sedime nts,Gibson’s solution applied to backfilling of mine stopes.Géotechnique 60,N o.11,877–882；
Helinski,M.,Fahey,M.,Fourie,A.2010b.Behaviour of cemented paste ba ckfill in two mine stopes,measurements and modeling.Journal of Geotechnical and Geoenvironmental Engineering,ASCE；137(2),171–182；
Helinski M,Fahey M,Fourie A.,2007b.Numerical modeling of cemented mine backfill deposition.Journal of Geotechnical and Geoenvironmental Engineer ing 133(10),1308–1319；
Helinski,M.,Fahey,M.,Fourie,A.2010a.Coupled two–dimensional finite element modelling of mine backfilling with cemented tailings.Canadian Geotech nical Journal 47,1187–1200；
Lu.G.2019.A model for one–dimensional deposition and consolidation of shrinking mine fills.Géotechnique Letters 7,347–351。
disclosure of Invention
Aiming at the defects of the prior art, the invention provides a method for simulating pore water pressure of a tailing filling body in high Wen Caichang and application thereof.
In order to achieve the above object, the present invention adopts the following technical scheme:
a method for simulating pore water pressure of a tailing filling body in a high Wen Caichang scale, which comprises the following steps:
step 1, based on the pore thermoelastic theoretical framework of Selvadurai and Suvorov, establishing a filler non-isothermal pore water pressure control equation under creep loading conditions by taking into account water volume changes caused by hydration reaction water consumption (i.e. chemical shrinkage action):
wherein α represents the Biot coefficient, α=1-K d /K s K in the formula d For bulk modulus of the pack skeleton, n is porosity, K s And K w Bulk modulus of solid phase and water, respectively, p w Represents pore water pressure, t is the time of reaction, beta s And beta w The coefficients of thermal expansion of the solid phase and water, respectively, T representing the current temperature, ε v For volumetric strain, k is the permeability coefficient, η represents the dynamic viscosity of water, ε shf And zeta is the hydration degree, which is the total water consumption in the chemical reaction process.
Step 2, assuming that the Biot coefficient alpha is approximately 1, alpha 1,
taking a filling body unit as a research object, further removing a seepage term and simplifying the formula (1) as follows:
the formula (2) is a pore water pressure control equation of a filler unit in the triaxial hydration pressure chamber.
Step 3, in order to simulate the compression effect caused by the creep of surrounding rock, axial deformation with the rate j/s is applied to a filling body sample by utilizing a triaxial hydration pressure chamber, and the thermoelastic stress-strain relation of the filling body unit under the creep loading effect is expressed as follows:
wherein ε represents strain, E represents Young's modulus, σ ' represents effective stress, v is Poisson's ratio, T 0 Indicating the initial temperature.
Step 4, establishing a geometric model of the filling body under the one-dimensional lateral limit condition, so that the filling body unit only has axial strain, and the effective stress in the x and y directions is equal, and the following relationship is established:
the volumetric deformation of the filler unit is thus obtained by the union (3) and the formula (4):
the parameters in formula (5) are expressed as:
step 5, under given confining pressure conditions, the change in effective stress is equal to the change in pore water pressure, i.e
Assuming that the solid phase compression is negative, equation (5) is therefore written as the derivative form:
and 6, substituting the formula (7) into the formula (2) on the premise of small strain assumption to finally obtain a pore water pressure control equation of the filler unit under the non-isothermal condition:
step 7, assuming that the triaxial hydration pressure chamber is completely insulated, that is, the filler unit cannot generate heat conduction and convection with the surrounding environment, the temperature change of the filler under the condition of thermal insulation and non-drainage is generated only by hydration heat release and the temperature load applied by the triaxial device, and further define the temperature of the filler as:
wherein k represents a constant rate of temperature change, T, applied by the triaxial apparatus h For the temperature rise caused by hydration reaction, Q f Is the heat evolved during the chemical reaction, (ρC) eff Representing the effective heat capacity ((ρC) eff ＝(1–n)ρ s C s +nρ w C w )，C s And C w Specific heat capacity, ρ, of solid-liquid two phases respectively s And ρ w The density of the solid phase and water, respectively.
Step 8, hydration degree and reference reaction time t e The relationship of (2) is expressed as:
ξ＝1-exp(-κ ξ ·t e ) (10)
wherein, kappa ξ Is the evolution rate of hydration level with reference time.
Step 9, according to the Arrhenius Wu Sigong formula, the actual time t and the reference time t e The relationship of (2) is expressed as:
wherein E is a Represents the activation energy required for chemical reactions, R a Is a universal gas constant (R) a ＝8.314J/mol/K)， T r Is the reference temperature.
further, the invention describes the growth evolution of the filler skeletal stiffness during hydration using the following formula:
K d ＝K di [λ-(λ-1)exp(-κ K ·t e )] (13)
k in the formula di The initial skeleton rigidity of the filler is lambda is the ratio of the final rigidity of the filler to the initial rigidity, kappa K To control the rate of stiffness increase.
Further, the evolution law of the thermal expansion coefficient of water with temperature is described by using the following formula
β w ＝β w0 +k 0 T (14)
Beta in w0 And k 0 Is a fitting parameter.
The invention also discloses application of the tailing filling body pore water pressure simulation method in the high Wen Caichang in the technical field of tailing filling exploitation.
Compared with the prior art, the invention has the advantages that:
the method has the advantages that complete knowledge is built for the first time aiming at the behavior response rule of the filling body under the condition of complex temperature environment, the behavior mechanism of the filling body under the action of temperature load is further deeply disclosed, the pressure increase induced by deep complex geothermal environment and the water pressure evolution rule of the filling body under the competing action of dissipation mechanism can be more accurately predicted, and further more scientific theoretical guidance is provided for providing a customized filling optimization scheme and realizing sustainable development of deep mineral resources.
Drawings
FIG. 1 is a schematic diagram showing the evolution law of pore water pressure with initial temperature at different moments according to the embodiment of the invention;
FIG. 2 is a schematic diagram showing the evolution law of the thermal expansion coefficients of water and a solid framework with temperature according to the embodiment of the invention;
FIG. 3 is a schematic diagram showing the temperature change of the filler units with different initial temperatures under the action of different heating and cooling rates according to the embodiment of the invention;
FIG. 4 is a graph showing the variation of water pressure of the filling body with different initial temperatures under the action of different heating and cooling rates according to the embodiment of the invention; (a) heating action (b) cooling action.
Detailed Description
The invention will be described in further detail below with reference to the accompanying drawings and by way of examples in order to make the objects, technical solutions and advantages of the invention more apparent.
The tailing filling body pore water pressure simulation method in the height Wen Caichang is based on a pore thermoelastic theory framework of Selvadurai and Suvoro v, and a filling body non-isothermal pore water pressure control equation is established by taking water volume change caused by hydration reaction water consumption (namely chemical shrinkage action) into consideration:
wherein α represents the Biot coefficient (α=1-K d /K s K in the formula d Bulk modulus of the pack skeleton), n is porosity, K s And K w Bulk modulus of solid phase and water, respectively, p w Represents pore water pressure, t is the time of reaction, beta s And beta w The coefficients of thermal expansion of the solid phase and water, respectively, T representing the current temperature, ε v For volumetric strain, k is the permeability coefficient, η represents the dynamic viscosity of water, ε shf And zeta is the hydration degree, which is the total water consumption in the chemical reaction process.
Due to the compressibility of the solid particles being negligible compared to the packing framework (i.e. K d <<K s ) It can therefore be assumed that the Biot coefficient a is approximately 1 (a 1,
). Meanwhile, as the invention mainly focuses on the influence effect of temperature load on pore water pressure of the filler, the filler unit can be used as a research object, so that seepage items are eliminated and the formula (1) is simplified as follows:
the formula (2) is a pore water pressure control equation of a filler unit in the triaxial hydration pressure chamber. Furthermore, considering the thermal expansion effect in a non-isothermal process, the thermoelastic stress-strain relationship of the filler unit can be expressed as:
wherein ε represents strain, E represents Young's modulus, σ ' represents effective stress, v is Poisson's ratio, T 0 Indicating the initial temperature.
In order to simplify the calculation, the present embodiment further establishes a geometric model of the filler under the one-dimensional constraint condition, so that the filler unit has only axial strain, and the effective stresses in the x and y directions are equal, and the following relationship holds:
the volumetric deformation of the filler unit can thus be obtained by the union of (3) and (4):
the parameters in formula (5) can be expressed as:
the change in effective stress at a given confining pressure is equal to the change in pore water pressure (i.e
Assuming negative solid phase compression), equation (5) can be written as the derivative form:
finally, substituting the formula (7) into the formula (2) can finally obtain the pore water pressure control equation of the filler unit under the non-isothermal condition on the premise of small strain assumption:
furthermore, the present embodiment assumes that the triaxial hydration pressure chamber is completely insulated, i.e. the filler unit cannot generate heat conduction and convection with the surrounding environment, so that the change in the temperature of the filler in the adiabatic non-drainage condition is generated only by the hydration heat release and the temperature load applied by the triaxial apparatus, and the filling body temperature can be defined as:
wherein k represents a constant rate of temperature change, T, applied by the triaxial apparatus h For the temperature rise caused by hydration reaction, Q f Is the heat evolved during the chemical reaction, (ρC) eff Representing the effective heat capacity ((ρC) eff ＝(1–n)ρ s C s +nρ w C w )，C s And C w Specific heat capacity, ρ, of solid-liquid two phases respectively s And ρ w The density of the solid phase and water, respectively.
According to the research of Doherty and Muir Wood, the hydration degree and the reference reaction time t e The relationship of (2) can be expressed as:
ξ＝1-exp(-κ ξ ·t e ) (24)
wherein, kappa ξ Is the evolution rate of hydration level with reference time.
According to Arrhenii Wu Sigong, the actual time t and the reference time t e The relationship of (2) can be expressed as:
wherein E is a Chemical representationThe activation energy required for the reaction, R a Is a universal gas constant (R) a ＝8.314J/mol/K)， T r Is the reference temperature. K (K)
Thus, taking equations (9) - (11) into equation (8), the pore water pressure control equation for the packing unit under temperature loading can be finally obtained:
the invention uses the following formula to describe the growth and evolution of the rigidity of the filler framework in the hydration process:
K d ＝K di [λ-(λ-1)exp(-κ K ·t e )] (27)
k in the formula di The initial skeleton rigidity of the filler is lambda is the ratio of the final rigidity of the filler to the initial rigidity, kappa K To control the rate of stiffness increase.
In addition, the evolution law of the thermal expansion coefficient of water with temperature is described by using the following formula
β w ＝β w0 +k 0 T (28)
Beta in w0 And k 0 Is a fitting parameter.
Filler pore water pressure evolution law under different temperature environment conditions
1) Influence of the initial temperature
Taking the example of a tailings packing used in the kanown Belle gold mine in australia, the physicochemical parameters are shown in table 1. The evolution law of pore water pressure of the filling body unit in the adiabatic non-drainage environment under different initial temperature conditions is shown in figure 1. Fig. 1 shows that the water pressure of the filler at any time decreases and then increases with the increase of the initial temperature. This is because raising the curing temperature of the low temperature filler will accelerate the chemical reaction rate, thereby promoting pore pressure dissipation due to hydration water consumption; meanwhile, since the thermal expansion coefficient of water is still small at a low temperature (fig. 2), the thermal expansion effect caused by hydration heat release is not obvious, so that the pore water pressure is continuously reduced with the initial temperature under the dominant action of hydration water consumption. However, as the curing temperature continues to rise, the thermal expansion coefficient of the water will continue to increase as the chemical reaction rate of the filler will further increase (fig. 2). Therefore, when the temperature reaches a certain critical value, the hydrothermal pressurization effect caused by hydration heat release exceeds the hydration water consumption effect, so that the pore water pressure rises along with the rising of the initial temperature.
It can also be seen from fig. 1 that after a chemical reaction of sufficient length (t=1000 h), the pore water pressure increases almost monotonically with increasing initial temperature. This is because the hydration reaction at this point is substantially complete, i.e., the same temperature rise and chemical shrinkage of the filler under the hydration reaction occurs for different initial temperatures, but the filler will produce a higher pore pressure under the stronger hydrothermal pressurization effect due to the greater coefficient of thermal expansion of the water at high temperatures.
Furthermore, it can be noted from fig. 1 that the longer the chemical reaction time, the lower the critical initial temperature at which the pore water pressure is turned from drop to rise. This is because low temperatures reduce the rate of hydration heat release, so it takes longer to generate enough temperature rise that the thermal expansion effect completely counteracts the depressurization of the hydration water consumption.
TABLE 1 physicochemical parameters of the Australian Kanowna Belle gold ore filler
From the above discussion, it is clear that the effect of the initial temperature conditions on the evolution of pore water pressure in the pack is a result of competing hydration water consumption and hydration exotherms. Because the thermal expansion coefficient of water is smaller when the initial temperature is lower, the water pressure dissipation caused by hydration water consumption plays a main role; however, as the thermal expansion coefficient of water increases rapidly with the increase of temperature, the hydrothermal pressurization effect caused by hydration heat release will ultimately control the pore water pressure evolution of the filler.
2) Influence of temperature load
In this example, the initial temperature was set to 0, 15, and 30℃by changing the rate of change of the filler cells at different forced temperatures (k=0, + -2.5X10) -3 、±5.0×10 -3 The numerical analysis is carried out in the water pressure change process under the condition of the temperature/h), so that the influence mechanism of the temperature load on the pore water pressure of the filler unit is researched.
The law of temperature change of the filler units with different initial temperatures under the conditions of different heating and cooling rates is shown in fig. 3. FIG. 3 shows that when k > 0℃per hour, the initial temperatures of the charge bodies at 15℃and 30℃are lower than the low temperature (T 0 The =0deg.C state produced a more pronounced temperature rise. This is because the higher the initial temperature, the faster the chemical reaction rate, and therefore the filler temperature will rise sharply under the combined effect of the exothermic hydration and forced heating. As the hydration reaction is completed gradually, the rate of temperature rise of the pack will drop off as the exothermic heat of hydration slows and eventually converge to a constant external heating rate. When k < 0 ℃ C./h, the cooling effect will strongly suppress the low-temperature filler (T) because the lower the initial temperature, the slower the chemical reaction rate 0 Temperature rise due to hydration exotherm =0℃. In contrast, a charge having an initial temperature of 15 ℃ and 30 ℃ will still produce a significant temperature rise early in the cool down due to the faster hydration heat release rate. However, as the hydration reaction is gradually completed, the temperature change of the pack will eventually be controlled by forced cooling.
The law of the evolution of water pressure of the filler units in the adiabatic non-drainage environment under the action of temperature load is shown in fig. 4 (a) and fig. 4 (b). Fig. 4 (a) shows that the filling bodies with initial temperatures of 15 ℃ and 30 ℃ both produced a significant increase in water pressure under heating compared to the constant temperature state (k=0 ℃/h). This is because, although the increase in temperature caused by heating accelerates chemical shrinkage and thus promotes pore pressure dissipation, the pressure reduction effect caused by hydration water consumption is difficult to counteract the hydrothermal pressurizing effect caused by temperature rise due to the large thermal expansion coefficient of water at high temperature, and thus pore water pressure is gradually increased in the heating process. It can also be seen from fig. 4 that a higher initial temperature charge will produce an earlier and faster water pressure increase at the same heating rate, since the coefficient of thermal expansion of water will increase with increasing temperature (fig. 2). In contrast, since the thermal expansion coefficient of water is extremely small at an initial temperature of 0 ℃, the promotion effect of temperature rise on hydration water consumption exceeds the hydrothermal supercharging effect, so that the pore water pressure is slightly lower than the constant temperature state in the early stage of heating. However, as the hydration reaction is gradually completed, the continued heating will still produce a significant hydrothermal pressurization effect, and therefore the pore water pressure of the pack will eventually be higher than in the isothermal state. The above calculations indicate that the tailings packing in the high Wen Cai void area will likely create a higher long term earth pressure on the retaining wall, as the packing will eventually produce a significant hydrothermal pressurization effect with continued heating.
Under the cooling effect, the pore water pressure at the initial temperatures of the filler at 15 ℃ and 30 ℃ is rapidly reduced along with the temperature drop (fig. 4 (b)). This is because, although cooling down suppresses the hydration water consumption rate, the thermal expansion coefficient of water is large at high temperature, and thus the cooling shrinkage of the filler eventually has a significant promoting effect on pore pressure dissipation. In contrast, since the thermal expansion coefficient of water is very small at an initial temperature of 0 ℃, the cooling shrinkage effect of the pore fluid in the cooling process is not obvious; meanwhile, the cooling effect also strongly inhibits hydration water consumption reaction so as to slow down pore pressure dissipation rate, so that the pore water pressure of the filler at the initial temperature of 0 ℃ is slightly higher than that of a constant temperature state in early cooling. However, as the hydration reaction is gradually completed, the cooling shrinkage caused by the temperature reduction will gradually dominate the water pressure change of the filler, so the pore water pressure will eventually be lower than the constant temperature state due to the continuous cooling effect. The above calculation results show that, although the low-temperature environment can inhibit hydration water consumption and is unfavorable for pore pressure dissipation, the filling operation in the low-temperature goaf is generally safer because the cooling process of the filling body can lead to fluid shrinkage and thus to a remarkable depressurization effect.
From the above discussion, the continuous heat exchange between the filler and the high Wen Weiyan also induces thermal strain and affects the hydraulic evolution. When the initial temperature of the filling body is high, the water pressure change caused by heat exchange plays a role in controlling the water pressure evolution due to the large thermal expansion coefficient of water. However, when the temperature of the filling body is low, the thermal strain caused by heating or cooling will also have a certain influence on the pore water pressure, but the water expansion coefficient is very small at low temperature, so the hydration water consumption rate change caused by heat exchange will dominate the early water pressure evolution of the filling body. However, as the chemical reaction is gradually completed, the pore water pressure of the cryofiller will eventually be controlled by the thermal strain created by the continuous heat exchange.
Those of ordinary skill in the art will appreciate that the embodiments described herein are intended to aid the reader in understanding the practice of the invention and that the scope of the invention is not limited to such specific statements and embodiments. Those of ordinary skill in the art can make various other specific modifications and combinations from the teachings of the present disclosure without departing from the spirit thereof, and such modifications and combinations remain within the scope of the present disclosure.
Claims (4)
1. The method for simulating the pore water pressure of the tailing filling body in the height Wen Caichang is characterized by comprising the following steps of:
step 1, based on a pore thermoelastic theoretical framework of Selvadurai and Suvorov, establishing a filler non-isothermal pore water pressure control equation under creep loading conditions by considering water volume change caused by hydration reaction water consumption:
wherein α represents the Biot coefficient, α=1-K d /K s K in the formula d For bulk modulus of the filler, n is porosity, K s And K w Bulk modulus of solid phase and water, respectively, p w Represents pore water pressure, t is the time of reaction, beta s And beta w The coefficients of thermal expansion of the solid phase and water, respectively, T representing the current temperature, ε v For volumetric strain, k is the permeability coefficient, η represents the dynamic viscosity of water, ε shf Is the total water consumption in the chemical reaction process, and ζ is the hydration degree;
step 2, assuming that the Biot coefficient alpha is approximately 1, alpha 1,
taking a filling body unit as a research object, further removing a seepage term and simplifying the formula (1) as follows:
the formula (2) is a filler pore water pressure control equation in the triaxial hydration pressure chamber;
step 3, in order to simulate the compression effect caused by the creep of surrounding rock, axial deformation with the rate j/s is applied to a filling body sample by utilizing a triaxial hydration pressure chamber, and the thermoelastic stress-strain relation of the filling body unit under the creep loading effect is expressed as follows:
wherein ε represents strain, E represents Young's modulus, σ ' represents effective stress, v is Poisson's ratio, T 0 Indicating an initial temperature;
step 4, establishing a geometric model of the filling body under the one-dimensional lateral limit condition, so that the filling body unit only has axial strain, and the effective stress in the x and y directions is equal, and the following relationship is established:
the volumetric deformation of the filler unit is thus obtained by the union (3) and the formula (4):
the parameters in formula (5) are expressed as:
step 5, under given confining pressure conditions, the change in effective stress is equal to the change in pore water pressure, i.e
Assuming that the solid phase compression is negative, equation (5) is therefore written as the derivative form: />
And 6, substituting the formula (7) into the formula (2) on the premise of small strain assumption to finally obtain a pore water pressure control equation of the filler unit under the non-isothermal condition:
step 7, assuming that the triaxial hydration pressure chamber is completely insulated, that is, the filler unit cannot generate heat conduction and convection with the surrounding environment, the temperature change of the filler under the condition of thermal insulation and non-drainage is generated only by hydration heat release and the temperature load applied by the triaxial device, and further define the temperature of the filler as:
wherein k represents a constant rate of temperature change, T, applied by the triaxial apparatus h For the temperature rise caused by hydration reaction, Q f Is the heat evolved during the chemical reaction, (ρC) eff Representing effective heat capacity, i.e. ρC eff ＝(1–n)ρ s C s +nρ w C w ，C s And C w Specific heat capacity, ρ, of solid-liquid two phases respectively s And ρ w Respectively are provided withIs the density of the solid phase and water;
step 8, hydration degree and reference reaction time t e The relationship of (2) is expressed as:
ξ＝1-exp(-κ ξ ·t e ) (10)
wherein, kappa ξ Is the evolution rate of hydration degree along with the reference time;
step 9, according to the Arrhenius Wu Sigong formula, the actual time t and the reference time t e The relationship of (2) is expressed as:
wherein E is a Represents the activation energy required for chemical reactions, R a Is a general gas constant, R a ＝8.314J/mol/K，T r Is the reference temperature;
step 10, carrying the formulas (9) - (11) into the formula (8), and finally obtaining a pore water pressure control equation of the filler unit under the action of temperature load:
2. a method for simulating pore water pressure of a tailings pond in a height Wen Caichang as claimed in claim 1, wherein: the growth evolution of the filler skeletal stiffness during hydration is described using the following formula:
K d ＝K di [λ-(λ-1)exp(-κ K ·t e )] (13)
k in the formula di The initial skeleton rigidity of the filler is lambda is the ratio of the final rigidity of the filler to the initial rigidity, kappa K To control the rate of stiffness increase.
3. A method for simulating pore water pressure of a tailings pond in a height Wen Caichang as claimed in claim 1, wherein: describing the evolution law of the thermal expansion coefficient of water along with the temperature by using the following formula
β w ＝β w0 +k 0 T (14)
Beta in w0 And k 0 Is a fitting parameter.
4. A method for simulating pore water pressure of a tailings pond in a height Wen Caichang as claimed in claim 1, wherein: the method is applied to the technical field of tailing filling and mining.
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