CN115422684B - Drilling non-submerged jet fluidization mining process parameter design method - Google Patents
Drilling non-submerged jet fluidization mining process parameter design method Download PDFInfo
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- 239000002893 slag Substances 0.000 claims description 12
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Abstract
The invention discloses a drilling non-submerged jet fluidization mining process parameter design method, which comprises the steps of jet pump structure size design, fluidization mining process parameter design, process matching degree verification and the like. According to the invention, the influence of particles in jet pump lifting ore pulp on jet pump efficiency is considered, a liquid-solid jet pump performance basic equation is perfected, the jet pump structure size is designed based on the improved liquid-solid jet pump performance basic equation, the corresponding jet pump structure size when the jet pump working efficiency is close to peak efficiency is determined, fluidization mining process parameters are matched and designed on the basis, and the actual flow ratio of the jet pump is compared with cavitation flow ratio to obtain optimal matching parameters, so that the design result can meet the requirement that high-pressure water jet in the fluidization mining process can finish ore body crushing operation in a non-submerged state, the fluidization mining efficiency is further improved, and theoretical guidance and data support can be provided for popularization and application of a non-submerged jet fluidization mining method.
Description
Technical Field
The invention relates to a parameter optimization method, in particular to a drilling non-submerged jet fluidization mining process parameter design method, and belongs to the technical field of fluidization mining.
Background
Fluidized mining is a mining method that ores are cut and crushed by high-pressure water jet through drilling, ore pulp is formed on a working surface and is lifted to the surface through drilling, and the ore pulp is sent to a concentrating mill for processing. The fluidized mining can be used for mining nonferrous metals and rare metal placers with shallow burial and small thickness, loose and porous mineral deposits with weak cementation, such as peat, coal, apatite, loose manganese ore, soft bauxite, asphaltic sandstone, gold iron placer, sedimentary oil deposit and the like, and can also be used for mining mineral deposits which are deeply buried and used as building materials, and is an effective mining method for sand, gravel and sand ore at the lower part of a permanent frozen soil layer.
In general, fluidization mining adopts a double-wall drill rod as a carrier, adopts high-pressure water jet to realize mineral crushing, and finishes the lifting of ore pulp through a jet pump. As shown in fig. 1, the outer flow passage of the double-wall drill rod is a high-pressure water passage, and the high-pressure water is a power source for crushing minerals and lifting ore pulp in the fluidization mining process, on one hand, the high-pressure water forms high-pressure water jet flow through a hydraulic cutting nozzle to crush ore bodies, on the other hand, the high-pressure water forms pressure difference between a nozzle outlet and a drilling annulus after being sprayed out of a jet pump nozzle, and the ore pulp is sucked into the inner flow passage of the double-wall drill rod under the action of the pressure difference, so that the ore pulp is lifted. In addition, a plurality of turbulent flow nozzles can be arranged at the bottom of the double-wall drill rod, the jet flow of the turbulent flow nozzles disturbs ore pulp falling into the bottom of the well, and the suction resistance of the jet pump to mineral particles at the bottom of the well is reduced.
Slurry lifting in vertical drilling is a central problem to be solved by the fluidized mining process. The resistance to be overcome by vertical drilling ore pulp lifting mainly comprises static pressure energy of ore pulp from the bottom of a drilling well to the ground, ore pulp along-path loss in a flow passage in a double-wall drill rod and ore pulp dynamic pressure. In existing fluidization mining processes, the slurry level in the double-wall drill pipe and the well annulus needs to be controlled to the vicinity of the well head. The dead weight of the slurry column in the drilling annulus is balanced with the static pressure energy required by the slurry lifting, so that the total slurry lifting resistance is reduced. Although controlling the vicinity of the drilling well head at the slurry level in the drilling annulus is an effective way to achieve vertical drilling slurry lifting, such a solution would allow high pressure water to pass through the slurry environment first after being ejected from the jet nozzles, again impacting the ore body, which would mean that the fluidization mining is submerged jet breaking up of the ore body. For submerged jet, after being sprayed out from the nozzle, the high-pressure water jet is mixed with ore pulp, the axial velocity of the jet is in a negative exponential decay law, and the impact force of the high-pressure water jet is greatly weakened. Therefore, the single well breaking radius and the production efficiency of the submerged jet fluidization mining process are low, and the popularization and the application of the fluidization mining process are limited.
In consideration of the cost of well formation in surface drilling and the economic benefit of the fluid mining process, high-pressure gas can be injected into the well annulus during fluid mining to force the liquid level in the well annulus to drop below a jet coal (rock) breaking nozzle, so that high-pressure water jet is used for breaking ore bodies in a non-submerged state. Notably, the reliable non-submerged jet coal (rock) breaking process should be such that the high pressure water jet is always in a non-submerged state during the fluidized mining process to complete the breaking operation. Thus stabilization of the slurry level in the well annulus is an important goal of non-submerged jet fluidization mining processes. Because the high-pressure water jet coal (rock) breaking process and the jet pump ore pulp lifting process are synchronous in time, the high-pressure water jet coal (rock) breaking process and the jet pump ore pulp lifting process are required to have high process matching performance. The lifting performance of the jet pump ensures that newly added ore pulp can be transported to the ground in time, and the operation environment of high-pressure water jet coal breaking is prevented from being changed from a non-submerged state to a submerged state. Therefore, researching the matching of the fluidization mining process has important practical significance for popularization and application of the non-submerged jet fluidization mining method.
The non-submerged jet fluidization mining process matching mainly comprises two aspects of jet pump structural dimension and fluidization mining process parameter design. In one aspect, a jet pump is a fluid machine that uses turbulent diffusion to transfer energy and mass. However, the maximum defect of the jet pump is low peak lifting efficiency, and researches show that the maximum lifting efficiency of the jet pump is only 35%. Therefore, ensuring that the lifting efficiency of the jet pump approaches to the peak lifting efficiency is important to improving the economic benefit of the application of the jet pump. Since there are no moving parts inside the jet pump, the structural size of the jet pump is an important influencing factor for the lifting performance of the jet pump. At present, researchers develop a great deal of influence researches on the efficiency of the jet pump by the structural size of the jet pump, and put forward an optimal jet pump performance equation empirical formula suitable for the same medium of working fluid and sucked fluid. When particles are contained in the fluid, the velocity slip between the particles and the fluid has a great influence on the performance of the jet pump. The conventional experimental formula of the optimal performance equation of the jet pump does not consider the key factor, and is difficult to guide the structural design of the jet pump in a liquid-solid system. On the other hand, the design of the fluidization mining process parameters should meet the requirement of high-pressure water jet on non-submerged coal (rock) breaking, namely the suction capacity of a jet pump is matched with the ore pulp production capacity, so that the stability of the ore pulp liquid level in a drilling annulus in the non-submerged fluidization mining process is maintained. In addition, because the actual suction flow of the jet pump to the ore pulp is directly related to the fluidized mining process parameters, such as high-pressure water pressure, coal seam burial depth and the like, the fluidized mining process parameters still need to be matched and designed on the basis of obtaining the optimal structural size of the jet pump. However, no related research has been reported on the design method of the technological parameters of the non-submerged jet fluidization mining of the drilling based on the jet pump at present.
Disclosure of Invention
Aiming at the problems in the prior art, the invention provides a drilling non-submerged jet fluidization mining process parameter design method, which can realize the matching of the lifting performance of a jet pump and the fluidization mining speed in a non-submerged state, further realize the completion of ore body breaking operation of high-pressure water jet in the non-submerged state in the fluidization mining process, improve the fluidization mining efficiency, and provide theoretical guidance and data support for the popularization and application of the non-submerged jet fluidization mining method.
In order to achieve the purpose, the method for designing the technological parameters of the drilling non-submerged jet fluidization mining specifically comprises the following steps:
Step1, designing the structural size of a jet pump: setting initial values of a jet pump area ratio m and a flow ratio q according to empirical values, and determining the corresponding jet pump structure size and the jet pump theoretical pressure ratio h including the jet pump nozzle outlet diameter D 1 when the jet pump working efficiency eta is close to eta max based on the jet pump peak efficiency eta max corresponding to the jet pump area ratio m;
Step2, fluidized mining process parameter design: on the basis of the structural size of the jet pump obtained in Step1, optimal fluidization mining technological parameters are optimized by combining the mineral seam occurrence conditions and the drilling tool conditions;
Step2-1, presetting an initial value of the hydraulic cutting nozzle outlet diameter D jet and an initial value of the turbulent nozzle outlet diameter D subjet according to the flow ratio q and the jet pump nozzle outlet diameter D 1, and adjusting the high-pressure water pressure P pumb and the back pressure P b to enable the actual jet pump pressure ratio h 'of the fluidization mining process to be as close to the theoretical jet pump pressure ratio h as possible, and to meet h' < h;
Step2-2, adjusting the outlet diameter D jet of the hydraulic cutting nozzle and the outlet diameter D subjet of the turbulent nozzle so that the actual flow ratio q 'of the jet pump in the fluidization mining process is as close as possible to the theoretical flow ratio q of the jet pump, and q' < q is satisfied;
Step3, verifying process matching degree: the cavitation flow ratio q k is the maximum flow ratio that the jet pump does not generate cavitation under the premise of the given jet pump structure size, whether the actual flow ratio q 'of the jet pump in the fluidization mining process is smaller than the cavitation flow ratio q k is verified, and if the actual flow ratio q' is smaller than the cavitation flow ratio q k, the jet pump structure size obtained by Step1 and the fluidization mining process parameter obtained by Step2 are the best matched parameters; if not, modifying the initial value of the jet pump area ratio m or the flow ratio q according to the empirical value, and repeating the steps Step1 to Step3 until the actual flow ratio q' of the jet pump in the fluidization mining process is smaller than the cavitation flow ratio q k.
Further, in Step1, when the fluid to be sucked is a liquid-solid system, the basic equation of the jet pump is:
Wherein: Is the flow velocity coefficient of the nozzle; /(I) Is the flow velocity coefficient of the throat; /(I)Is the flow velocity coefficient of the diffusion tube; /(I)Taking 0.95 for the flow velocity coefficient of the suction chamber; /(I)Taking 1 as a flow velocity coefficient of an inlet section of the throat pipe;
Mu 1 is the correction coefficient of the particle and liquid velocity slip of the outlet section of the suction chamber; mu 2 is the correction coefficient of the particle and liquid velocity slip of the throat inlet section; mu 3 is the correction coefficient of the particle and the liquid velocity slip of the throat outlet section;
a is a throat inlet function; c is the suction area ratio; q is the theoretical flow ratio; m is the area ratio; n is a coefficient related to the area ratio; delta is the fluid momentum correction coefficient of the throat outlet section; beta is the contraction half angle of the inlet section of the throat;
f 3 is the throat inlet area, unit m 2;f1 is the nozzle outlet area, unit m 2;fs1 is the flow area of the sucked fluid in the section of the suction chamber outlet, and unit m 2;
k 1 is the non-uniform coefficient of the flow velocity distribution of the working fluid at the inlet section of the throat, and 0.95 is taken; k' 1 is the non-uniform comprehensive coefficient of the flow velocity distribution of the working fluid at the inlet section of the throat; k 2 is the non-uniform coefficient of the flow velocity distribution of the sucked fluid at the inlet section of the throat, and 1.10 is taken; k' 2 is the non-uniform comprehensive coefficient of the flow velocity distribution of the working fluid at the inlet section of the throat; is the volume-weight ratio of the absorbed fluid to the working fluid.
Further, the correction coefficient μ 1 of the suction chamber outlet profile particle and liquid velocity slip is expressed as:
Wherein: c v is the particle volume concentration; the average flow velocity of the solid particles in the outlet section of the suction chamber is expressed in m/s; v s1 is the average flow velocity of the sucked fluid at the outlet section of the suction chamber under the influence of neglecting particles, and the unit is m/s; q s is the flow rate of the sucked fluid of the jet pump, the unit m 3/s;fs1 is the flow area of the sucked fluid in the section of the outlet of the suction chamber, the unit m 2;D1 is the diameter of the outlet of the nozzle of the jet pump, and the unit m; l c is the throat distance, unit m; m is the area ratio; beta is the contraction half angle of the inlet section of the throat; v ss is the fluid flow rate at the suction port, in m/s; f drags is the drag force exerted by the slurry suction port particles, and the unit is N; g is the gravitational acceleration, unit m/s 2; a is the projection area of particles along the water flow direction, the unit m 2;a1 is the nozzle wall thickness correction coefficient, and 1.2 is taken; d p is the maximum particle diameter of particles at the slurry suction port, and the unit is m; gamma p particle volume weight, unit N/m 3;γs is fluid volume weight of the pulp suction port, unit N/m 3;Vp is volume of the maximum particle size particle at the pulp suction port, and unit m 3; /(I) The sedimentation end speed of the particles with the maximum particle size at the pulp suction port is in m/s; s is the area of a suction inlet, and the unit m 2;Ls is the length of a suction chamber and the unit m; c d is the drag coefficient of the particles, and 0.44 is taken;
The correction coefficient mu 2 of the throat inlet profile particle and the liquid velocity slip is expressed as:
Wherein: v s2 is the average flow velocity of the sucked fluid in the section of the throat inlet under the influence of neglecting particles, and the unit is m/s; The average flow velocity of the solid particles at the inlet section of the throat pipe is in units of m/s; f drag1 is the drag force exerted by the solid particles in the outlet section of the suction chamber, unit N; f 3 is the throat inlet area, unit m 2;f1 is the nozzle outlet area, unit m 2;γ1 is the volume weight of the fluid at the inlet section of the throat, and unit N/m 3;
The correction coefficient mu 3 of the throat outlet profile particle and the liquid velocity slip is expressed as:
Wherein: q is the theoretical flow ratio; v s3 is the average flow velocity of the fluid at the throat outlet section under the influence of neglected particles, in m/s; The average flow velocity of the solid particles at the section of the outlet of the throat pipe is expressed in m/s; f drag2 is the drag force exerted by the solid particles on the inlet section of the throat pipe, and the unit is N; gamma 2 is the volume weight of the fluid at the inlet of the throat pipe, the unit N/m 3;Q0 is the flow rate of the working fluid of the jet pump, and the unit m 3/s.
Further, in Step2-1, the jet pump actual pressure ratio h' is expressed as:
Pjetpumb＝ρliftgH+hlift+hv
Wherein: p jetpumb is the energy required by the ore pulp to be lifted to the ground without back pressure, and the unit Pa; ρ lift is the flow path pulp density in the double-wall drill pipe, unit kg/m 3; g is gravity acceleration, and m/s 2;hlift is the on-way resistance of the pulp in the flow path of the double-wall drill pipe, and the unit is Pa; h int is the along-the-way resistance of the double-wall drill rod outer flow channel water inlet pipe, and the unit is Pa; h v is the dynamic pressure of the pulp in the flow path in the double-wall drill pipe, and the unit Pa; h is the lifting height of ore pulp, and the unit is m; p b is hydraulic mining back pressure, unit Pa; p pumb is the pressure of high-pressure water, in Pa;
The slurry density ρ lift of the double-wall drill pipe inner flow path in the formula of the energy P jetpumb required for lifting the slurry to the ground under the condition of no back pressure is expressed as follows:
Wherein: ρ p is the mineral seam density in kg/m 3; ρ is the high-pressure water density, the unit kg/m 3;Qwater is the liquid flow rate in the sucked fluid in the slag returning pipe, the unit m 3/s;Qcoal is the particle flow rate in the sucked fluid in the slag returning pipe, the unit m 3/s;Q'0 is the working fluid flow rate of the jet pump in the fluidization mining process, the unit m 3/s;Q's is the sucked fluid flow rate of the jet pump in the fluidization mining process, and the unit m 3/s;
the dynamic pressure h v of the pulp in the flow path in the double-wall drill pipe in the formula of the energy P jetpumb required for lifting the pulp to the ground under the condition of no back pressure is expressed as follows:
Wherein: u lift is the flow rate of pulp in the flow path of the double-wall drill pipe, and the unit is m/s; a inner is the inner diameter of the double-wall drill rod, and the unit is m;
The energy P jetpumb formula required by lifting the ore pulp to the ground under the condition of no back pressure and the actual pressure ratio h' formula of the jet pump are expressed as the along-path resistance h lift of the ore pulp in the double-wall drill pipe inner flow passage and the along-path resistance h int of the water inlet pipe of the double-wall drill pipe outer flow passage:
wherein: lambda lift is the friction coefficient of the inner flow passage of the double-wall drill rod, and 0.04 is taken; d lift is the hydraulic diameter of the flow path in the double-wall drill rod, and the unit is m; lambda int is the friction coefficient of the outer flow passage of the double-wall drill rod, and 0.04 is taken; d int is the hydraulic diameter of the outer flow channel of the double-wall drill rod, and the unit is m; u int is the speed of the outer flow channel of the double-wall drill rod, and the unit is m/s.
Further, in Step2-2, the actual flow ratio q' of the jet pump is expressed as:
wherein: q' 0 is the jet pump working fluid flow; q' s is the flow rate of the fluid absorbed by the jet pump;
the jet pump working fluid flow rate Q '0 and the jet pump suction fluid flow rate Q' s are represented as:
Qs'＝Qwater+Qcoal
Wherein: u is the high-pressure water speed, and the unit is m/s; d 1 is the nozzle outlet diameter, in m; q water is the flow rate of liquid in the sucked fluid in the slag returning pipe, the unit m 3/s;Qcoal is the flow rate of particles in the sucked fluid in the slag returning pipe, the unit m 3/s;λjet is the flow rate coefficient of the nozzle, and the flow rate coefficient is 0.975; d jet is the diameter of the outlet of the hydraulic cutting nozzle, and the unit is m; d subjet is the outlet diameter of the turbulent nozzle, and the unit is m; p pumb is the pressure of high-pressure water, in Pa; ρ is the high pressure water density in kg/m 3; h is the lifting height of ore pulp, and the unit is m; p b is hydraulic mining back pressure, unit Pa; h int is the along-the-way resistance of the double-wall drill rod outer flow passage water inlet pipe, and the unit is Pa.
Further, in Step3, the cavitation flow rate ratio q k is expressed as:
Wherein: m is the area ratio of the jet pump; h k is cavitation pressure ratio; epsilon is the cavitation flow ratio coefficient;
Cavitation pressure ratio h k is expressed as:
Wherein: p a is the atmospheric pressure, unit Pa; p b is hydraulic mining back pressure, unit Pa; p pumb is the pressure of high-pressure water, in Pa; ρ lift is the flow path pulp density in the double-wall drill pipe, unit kg/m 3; g is the gravitational acceleration, unit m/s 2; h is the lifting height of ore pulp, and the unit is m; h int is the along-the-way resistance of the double-wall drill rod outer flow channel water inlet pipe, and the unit is Pa; p k is the saturated vapor pressure of water in Pa.
Compared with the prior art, the jet pump structure size and the drilling fluidization exploitation process parameters designed by the design method provided by the drilling non-submerged jet fluidization exploitation process parameter design method can meet the technical requirements of drilling non-submerged jet fluidization exploitation, namely the lifting capacity of the jet pump on ore pulp in the fluidization exploitation process is matched with the ore pulp production capacity of high-pressure water jet, and the jet pump is matched with the high-pressure gas with a certain pressure in the drilling annulus, so that the ore pulp liquid level in the drilling annulus can be ensured to be lower than the height of a jet coal breaking nozzle, the stability of the ore pulp liquid level in the drilling annulus is maintained in the fluidization exploitation process, and the drilling non-submerged jet fluidization exploitation is realized; in addition, compared with submerged jet, the axial velocity decay rate of the non-submerged jet under the same high-pressure water flow rate is obviously reduced, and the high-pressure water jet energy is more concentrated, so that the drilling non-submerged jet environment formed by the design method can greatly improve the single well exploitation radius of drilling fluidization exploitation, can obviously reduce the water consumption of fluidization exploitation process while guaranteeing the exploitation radius, has obvious fluidization exploitation efficiency and economic benefit, and can provide theoretical guidance and data support for popularization and application of the non-submerged jet fluidization exploitation method.
Drawings
FIG. 1 is a schematic illustration of a fluid mining;
FIG. 2 is a schematic diagram of a jet pump, wherein I is a nozzle, II is a throat inlet section, III is a throat, IV is a diffuser, V is a suction chamber, VI is a double-wall drill pipe outer flow passage, s-s section is a suction port section, c-c section is a diffuser outlet section, 0-0 section is a nozzle inlet section, 1-1 section is a suction chamber outlet section, 2-2 section is a throat inlet section, 3-3 section is a throat outlet section, and beta is a throat inlet section contraction half angle;
FIG. 3 is a flow chart of the present invention;
FIG. 4 is an enlarged view of a portion of the throat entrance of the jet pump;
fig. 5 is a diagram of a jet pump lift numerical calculation physical model, in which (a) is a boundary condition diagram, (b) is a whole model diagram, and (c) is a partial model diagram;
FIG. 6 is a jet pump axial pressure profile.
Detailed Description
The invention is further described below with reference to the accompanying drawings.
As shown in fig. 2, the key components of the jet pump of the fluidization mining process include a nozzle, a throat inlet section, a throat, a diffuser pipe and a suction chamber, and since the suction chamber is generally a channel structure with uniform diameter, the influence on the performance of the jet pump is small, the influence on the performance of the jet pump of the suction chamber is ignored, and the structural names of the other components required to be designed are shown in table 1.
TABLE 1 Critical component Structure of jet Pump
The jet pump lift performance can be expressed in terms of the following dimensionless quantities:
① Theoretical flow ratio q:
wherein: q s is the flow rate of the sucked fluid, unit m 3/s;Q0 is the flow rate of the working fluid, and unit m 3/s.
② Theoretical pressure ratio h:
Wherein: p c is the hydrostatic pressure at the outlet of the diffuser pipe, in Pa;
p s is the hydrostatic pressure of the suction port, unit Pa;
p 0 is the hydrostatic pressure of the working fluid inlet of the jet pump, and the unit Pa;
v c is the fluid flow rate at the outlet of the diffuser in m/s;
v s is the fluid flow rate of the suction port, in m/s;
v 0 is the fluid flow rate of the jet pump working fluid inlet, in m/s;
z c is the height of the outlet of the diffuser in m;
z s is the height of the suction port, unit m;
z 0 is the height of the jet pump working fluid inlet, in m;
gamma c is the volume weight of the fluid at the outlet of the diffusion pipe, and the unit is N/m 3;
Gamma s is the fluid volume weight of the suction port, unit N/m 3;
Gamma 0 is the fluid volume weight of the jet pump working fluid inlet in N/m 3.
③ Area ratio m:
wherein: f 3 is throat inlet area, unit m 2;f1 is nozzle outlet area, unit m 2.
④ Efficiency eta:
The jet pump performance equation is a functional relationship that must be satisfied between the pressure ratio, flow ratio, area ratio, and critical component structural dimensions of the jet pump to ensure that the jet pump can lift the fluid being sucked to the target position. In addition, when in fluidization mining, the jet pump is limited by a drilling space, and the jet pump structural design not only meets the basic equation of the jet pump, but also needs to ensure that the lifting efficiency of the jet pump to ore pulp is matched with the crushing efficiency of high-pressure water jet to a mineral seam so as to ensure the fluidization mining efficiency.
As shown in fig. 3, the method for designing the technological parameters of the drilling non-submerged jet fluidization mining comprises the following steps:
Step1, designing the structural size of a jet pump: and (3) setting initial values of the area ratio m and the flow ratio q of the jet pump according to empirical values, and then determining the corresponding structural size of the jet pump and the theoretical pressure ratio h of the jet pump when the working efficiency of the jet pump is highest by changing variable parameters of the jet pump.
The satisfaction of the basic equations of the jet pump among the pressure ratio of the jet pump, the flow ratio and the structural dimensions of the key components is a necessary and insufficient condition for the jet pump to lift the sucked fluid to the target position. When the absorbed fluid is a liquid-solid system, the basic equation of the jet pump is as follows:
Wherein: Is the flow velocity coefficient of the nozzle;
Is the flow velocity coefficient of the throat;
Is the flow velocity coefficient of the diffusion tube;
taking 0.95 for the flow velocity coefficient of the suction chamber;
The flow velocity coefficient of the throat inlet is related to the friction coefficient of the throat inlet, and the friction loss of the throat inlet can be ignored due to the shorter throat inlet, so/>
Mu 1 is the correction coefficient of particle and liquid velocity slip in the suction chamber outlet profile (1-1 profile in FIG. 2);
Mu 2 is the correction coefficient of particle and liquid velocity slip of the throat inlet section (section 2-2 in FIG. 2);
mu 3 is the correction coefficient of particle and liquid velocity slip in the throat outlet profile (3-3 profile in FIG. 2);
a is a throat inlet function;
c is the suction area ratio;
q is the flow ratio;
m is the area ratio;
n is a coefficient related to the area ratio;
delta is the fluid momentum correction coefficient of the throat outlet profile (3-3 in fig. 2);
beta is the contraction half angle of the inlet section of the throat (shown in figure 2);
f 3 is throat inlet area, unit m 2;
f 1 is the nozzle exit area, unit m 2;
f s1 is the flow area of the sucked fluid in the outlet section of the suction chamber, unit m 2;
k 1 is the non-uniform coefficient of the flow velocity distribution of the working fluid at the inlet section of the throat, and 0.95 is taken;
k' 1 is the non-uniform comprehensive coefficient of the flow velocity distribution of the working fluid at the inlet section of the throat;
k 2 is the non-uniform coefficient of the flow velocity distribution of the sucked fluid at the inlet section of the throat, and 1.10 is taken;
k' 2 is the non-uniform comprehensive coefficient of the flow velocity distribution of the working fluid at the inlet section of the throat;
is the volume-weight ratio of the absorbed fluid to the working fluid.
To calculate the slip velocity of the particles and fluid in the jet pump, a drag model is introduced into the calculation of the particle velocity in the jet pump, and as shown in fig. 4, the correction coefficient μ 1 of the slip of the particles and fluid velocity in the outlet section of the suction chamber can be expressed as:
Wherein: c v is the particle volume concentration;
Is the average flow velocity of solid particles in the outlet section of the suction chamber (section 1-1 in FIG. 2), in m/s;
v s1 is the average flow velocity in m/s of the sucked fluid at the suction chamber outlet section (section 1-1 in fig. 2) under the influence of neglecting particles;
Q s is the flow rate of the sucked fluid of the jet pump, and the unit is m 3/s;
f s1 is the flow area of the sucked fluid in the suction chamber outlet section (section 1-1 in fig. 2), unit m 2;
d 1 is the diameter of the outlet of the jet pump nozzle, and the unit is m;
L c is the throat distance, unit m;
m is the area ratio;
Beta is the contraction half angle of the inlet section of the throat;
v ss is the fluid flow rate at the suction port, in m/s;
F drags is the drag force exerted by the slurry suction port particles, and the unit is N;
g is the gravitational acceleration, unit m/s 2;
a is the projection area of the particles along the water flow direction, and the unit is m 2;
a 1 is a nozzle wall thickness correction coefficient, 1.2 is taken;
D p is the maximum particle diameter of particles at the slurry suction port, and the unit is m;
Gamma p particle volume weight, unit N/m 3;
Gamma s is the fluid volume weight of the suction port, unit N/m 3;
V p is the volume of the particles with the maximum particle diameter at the pulp suction port, and the unit is m 3;
The sedimentation end speed of the particles with the maximum particle size at the pulp suction port is in m/s;
S is the area of a pulp suction port, and the unit is m 2;
l s is the length of the suction chamber in m;
c d is the drag coefficient of the particles, taking 0.44.
The correction coefficient μ 2 for the throat inlet profile particle versus liquid velocity slip can be expressed as:
Wherein: v s2 is the average flow velocity in m/s of the sucked fluid at the throat inlet section (section 2-2 in FIG. 2) under the influence of neglected particles;
Is the average flow velocity of solid particles in the throat inlet section (section 2-2 in FIG. 2) in m/s;
f drag1 is the drag force exerted by the solid particles in the suction chamber outlet section (section 1-1 in FIG. 2), unit N;
f 3 is throat inlet area, unit m 2;
f 1 is the nozzle exit area, unit m 2;
Gamma 1 is the volume weight of the fluid at the inlet section of the throat, N/m 3.
The correction coefficient μ 3 for the throat outlet profile particle versus liquid velocity slip can be expressed as:
wherein: q is the theoretical flow ratio;
v s3 is the average flow velocity in m/s of the fluid at the throat outlet section (section 3-3 in FIG. 2) under the influence of neglected particles;
is the average flow velocity of solid particles in the throat outlet section (section 3-3 in FIG. 2), in m/s;
F drag2 is the drag force exerted by the solid particles at the throat inlet section (section 2-2 in FIG. 2), unit N;
Gamma 2 is the volume weight of the fluid at the inlet of the throat, and the unit is N/m 3;
Q 0 is the jet pump working fluid flow, unit m 3/s.
Step2, fluidized mining process parameter design: on the basis of the structural size of the jet pump obtained in Step1, optimal fluidization mining technological parameters are optimized by combining the mineral seam occurrence conditions and the drilling tool conditions.
In general, the inside and outside diameters of double-wall drill pipes used in fluid mining are fixed, so that matched fluid mining process parameters are designed according to the burial depth of a mineral seam and the condition of a drilling tool when fluid mining is implemented. The fluidization mining technological parameters mainly comprise high-pressure water pressure P pumb, hydraulic mining back pressure P b, hydraulic cutting nozzle outlet diameter D jet and turbulent nozzle outlet diameter D subjet, and the specific design steps are as follows:
Step2-1, presetting an initial value of the hydraulic cutting nozzle outlet diameter D jet and an initial value of the turbulent nozzle outlet diameter D subjet according to the flow ratio q and the jet pump nozzle outlet diameter D 1, and adjusting the high-pressure water pressure P pumb and the back pressure P b to enable the actual jet pump pressure ratio h 'of the fluidization mining to be as close to the theoretical jet pump pressure ratio h as possible, and to meet h' < h.
The physical meaning of the pressure ratio in the fluidization mining process is the ratio of the energy required by the slurry at the bottom of the well to be lifted to the ground to the total energy of the high-pressure water at the inlet of the jet pump. The jet pump actual pressure ratio h' in fluid mining can thus be expressed as:
Pjetpumb＝ρliftgH+hlift+hv
wherein: p jetpumb is the energy required by the ore pulp to be lifted to the ground without back pressure, and the unit Pa;
ρ lift is the flow path pulp density in the double-wall drill pipe, unit kg/m 3;
g is gravity acceleration, m/s 2;
h lift is the on-way resistance of the pulp of the flow path in the double-wall drill pipe, and the unit is Pa;
h int is the along-the-way resistance of the double-wall drill rod outer flow channel water inlet pipe, and the unit is Pa;
h v is the dynamic pressure of the pulp in the flow path in the double-wall drill pipe, and the unit Pa;
h is the lifting height of ore pulp, and the unit is m;
P b is hydraulic mining back pressure, unit Pa;
p pumb is the high-pressure water pressure, in Pa.
The double-wall drill pipe inner flow path pulp density ρ lift in the above formula of the energy required for pulp lifting to the ground without back pressure P jetpumb can be expressed as:
Wherein: ρ p is the mineral seam density in kg/m 3;
ρ is the high pressure water density in kg/m 3;
q water is the flow rate of liquid in the sucked fluid in the slag returning pipe, and the unit is m 3/s;
Q coal is the particle flow rate in the sucked fluid in the slag returning pipe, and the unit is m 3/s;
Q' 0 is the flow rate of the working fluid of the jet pump in the fluidized mining process, and the unit is m 3/s;
q' s is the flow rate of fluid absorbed by the jet pump in the fluidized mining process, and the unit is m 3/s.
The dynamic pressure h v of the slurry in the flow path in the double-wall drill pipe in the formula of the energy P jetpumb required for lifting the slurry to the ground under the condition of no back pressure can be expressed as follows:
Wherein: u lift is the flow rate of pulp in the flow path of the double-wall drill pipe, and the unit is m/s;
a inner is the inner diameter of the double-wall drill rod, and the unit is m.
The above formula of the energy P jetpumb required for lifting the ore pulp to the ground under no back pressure and the actual pressure ratio h' of the jet pump can be expressed as the along-path resistance h lift of the ore pulp in the double-wall drill pipe inner flow passage and the along-path resistance h int of the water inlet pipe of the double-wall drill pipe outer flow passage:
Wherein: lambda lift is the friction coefficient of the inner flow passage of the double-wall drill rod, and 0.04 is taken;
d lift is the hydraulic diameter of the flow path in the double-wall drill rod, and the unit is m;
Lambda int is the friction coefficient of the outer flow passage of the double-wall drill rod, and 0.04 is taken;
d int is the hydraulic diameter of the outer flow channel of the double-wall drill rod, and the unit is m;
u int is the speed of the outer flow channel of the double-wall drill rod, and the unit is m/s.
Step2-2, adjusting the hydraulic cutting nozzle outlet diameter D jet and the turbulent nozzle outlet diameter D subjet so that the jet pump actual flow ratio q 'of the fluidization mining process is as close as possible to the jet pump theoretical flow ratio q, and satisfies q' < q.
When the pulp lifting efficiency of the jet pump is matched with the high-pressure water jet coal breaking efficiency, the physical meaning of the actual flow ratio of the jet pump in the hydraulic mining process is the ratio of the sum of the high-pressure water flow and the coal dropping flow for jet coal breaking to the working fluid flow of the jet pump. That is, the jet pump actual flow ratio q' in a fluid mining process can be expressed as:
Wherein: q' 0 is the jet pump working fluid flow; q' s is the flow rate of the fluid being sucked by the jet pump.
The flow rate of coal falling per unit time in the fluidization mining process is about 10% of the flow rate of high-pressure water jet, and the flow rate Q '0 of the working fluid of the jet pump and the flow rate Q' s of the sucked fluid of the jet pump in the fluidization mining process can be expressed as follows:
Qs'＝Qwater+Qcoal
wherein: u is the high-pressure water speed, and the unit is m/s;
D 1 is the nozzle outlet diameter, in m;
q water is the flow rate of liquid in the sucked fluid in the slag returning pipe, and the unit is m 3/s;
Q coal is the particle flow rate in the sucked fluid in the slag returning pipe, and the unit is m 3/s;
Lambda jet is the nozzle flow rate coefficient, 0.975;
D jet is the diameter of the outlet of the hydraulic cutting nozzle, and the unit is m;
D subjet is the outlet diameter of the turbulent nozzle, and the unit is m;
p pumb is the pressure of high-pressure water, in Pa;
ρ is the high pressure water density in kg/m 3;
h is the lifting height of ore pulp, and the unit is m;
P b is hydraulic mining back pressure, unit Pa;
h int is the along-the-way resistance of the double-wall drill rod outer flow passage water inlet pipe, and the unit is Pa.
Step3, verifying process matching degree: the cavitation flow ratio q k is the maximum flow ratio that the jet pump does not generate cavitation under the premise of the given jet pump structure size, whether the actual flow ratio q 'of the jet pump for fluidization mining is smaller than the cavitation flow ratio q k is verified, and if the actual flow ratio q' is smaller than the cavitation flow ratio q k, the jet pump structure size obtained by Step1 and the fluidization mining technological parameters obtained by Step2 are the best matching matched parameters; if not, modifying the initial value of the jet pump area ratio m or the flow ratio q according to the empirical value, and repeating the steps Step1 to Step3 until the actual flow ratio q' of the jet pump for fluidization mining is smaller than the cavitation flow ratio q k.
Cavitation flow ratio q k may be expressed as:
wherein: m is the area ratio of the jet pump; h k is cavitation pressure ratio;
Epsilon is the cavitation flow ratio coefficient.
The cavitation pressure ratio h k in the cavitation flow ratio q k equation above may be expressed as:
Wherein: p a is the atmospheric pressure, unit Pa;
P b is hydraulic mining back pressure, unit Pa;
p pumb is the pressure of high-pressure water, in Pa;
ρ lift is the flow path pulp density in the double-wall drill pipe, unit kg/m 3;
g is the gravitational acceleration, unit m/s 2;
h is the lifting height of ore pulp, and the unit is m;
h int is the along-the-way resistance of the double-wall drill rod outer flow channel water inlet pipe, and the unit is Pa;
P k is the saturated vapor pressure of water in Pa.
The invention is further illustrated by the following examples.
Taking fluidization mining as an example of a coal bed with a certain coal mine burial depth of 425m, the inner diameter of a double-wall drill rod is 120mm, the annular clearance of the double-wall drill rod is 18mm, and the optimal jet pump structure size and the on-site process parameters in the coal bed fluidization mining process are shown in the following table 2 and the table 3 respectively according to the steps.
Table 2 structural parameters of jet pumps
| Parameter name | Numerical value | Parameter name | Numerical value |
| Area ratio m | 8 | Nozzle outlet diameter D 1 | 9.5mm |
| Flow ratio q | 2.18 | Nozzle length | 39mm |
| Suction port area S | 0.0018m2 | Length of throat Lt | 188mm |
| Number of pulp suction openings | 4 | Diameter D of throat 3 | 27mm |
| Laryngeal distance L c | 14.25mm | Diffusion tube length | 750mm |
| Shrinkage half angle beta of throat pipe inlet section | 30° | Diffusion tube outlet diameter D c | 120mm |
| Nozzle inlet diameter D 0 | 50mm | Theoretical pressure ratio h | 0.1117 |
TABLE 3 in situ process parameters
| Parameter name | Numerical value | Parameter name | Numerical value |
| High pressure water pressure P pumb | 17MPa | Diameter D of inner flow path of double-wall drill rod c | 120mm |
| Back pressure P b | 3.05MPa | Double-wall drill pipe outer flow channel gap | 18mm |
| Elevation H | 425m | Diffusion tube outlet pressure P k | 4.75MPa |
| Jet coal breaking nozzle diameter D jet | 13.2mm | Actual pressure ratio h' | 0.114 |
| Turbulent nozzle diameter D subjet | 1.5mm | Actual flow ratio q' | 2.17 |
| Turbulent flow nozzle number | 2 | Jet pump design promotes total flow | 34.11kg/s |
In order to verify the rationality of the design method of the drilling non-submerged jet fluidization mining process parameters, a numerical calculation model is adopted to verify the lifting performance of the jet pump. In order to reduce the calculation amount, the numerical calculation model only comprises a double-wall drill pipe inner runner. The diffuser and throat dimensions are as in Table 2 above, with a total riser length of 400mm. The numerical calculation physical model is shown in fig. 5. The numerical boundary conditions are shown in table 4 below.
Table 4 numerical calculation boundary conditions
| Boundary name | Numerical value (MPa) |
| Pressure inlet P int | 18.30 |
| Pressure inlet P b | 3.05 |
| Pressure outlet P out | 4.75 |
The total lifting flow of the jet pump is 33.16kg/s, and compared with the total lifting mass of 34.11kg/s of the jet pump, the relative error is only 2.79%, so that the method meets the design requirement of the drilling non-submerged jet fluidization mining process.
Furthermore, the peak operating efficiency of the jet pump is related to the area ratio m, and when the area ratio m=8, the peak operating efficiency of the jet pump is about 30%. Through calculation, when the area ratio of the jet pump is 8m, the lifting efficiency of the jet pump designed by the design method provided by the patent is 31.1%, which is equivalent to the peak efficiency of the jet pump under the same area ratio. Meanwhile, the axial pressure monitoring line of the jet pump is shown in fig. 5 (a). The jet pump pressure distribution along the pressure monitoring line is shown in fig. 6. As can be seen from fig. 6, the pressure of the high-pressure water after being ejected from the jet pump nozzle suddenly drops and decreases to a minimum value (2.05 MPa) at the throat inlet. The minimum pressure inside the jet pump is far greater than the saturated vapor pressure of water at normal temperature and pressure, which indicates that the jet pump of the embodiment cannot generate cavitation when lifting ore pulp.
The method for designing the drilling non-submerged jet fluidization mining technological parameters can obtain the optimal jet pump structural size and the on-site fluidization mining technological parameters matched with the jet pump structural size under the conditions of known mineral seam burial depth, double-wall drill rod size, mineral seam physical properties and the like, and the optimization result can meet the requirement that high-pressure water jet completes ore body crushing operation in a non-submerged state in the fluidization mining process, so that the fluidization mining efficiency is improved, and theoretical guidance and data support can be provided for popularization and application of the non-submerged fluidization mining method.
Claims (4)
1. The method for designing the drilling non-submerged jet fluidization mining technological parameters is characterized by comprising the following steps of:
Step1, designing the structural size of a jet pump: setting initial values of a jet pump area ratio m and a flow ratio q according to empirical values, and determining the corresponding jet pump structure size and the jet pump theoretical pressure ratio h including the jet pump nozzle outlet diameter D 1 when the jet pump working efficiency eta is close to eta max based on the jet pump peak efficiency eta max corresponding to the jet pump area ratio m;
Step2, fluidized mining process parameter design: on the basis of the structural size of the jet pump obtained in Step1, optimal fluidization mining technological parameters are optimized by combining the mineral seam occurrence conditions and the drilling tool conditions;
Step2-1, presetting an initial value of the hydraulic cutting nozzle outlet diameter D jet and an initial value of the turbulent nozzle outlet diameter D subjet according to the flow ratio q and the jet pump nozzle outlet diameter D 1, and adjusting the high-pressure water pressure P pumb and the back pressure P b to enable the actual jet pump pressure ratio h 'of the fluidization mining process to be as close to the theoretical jet pump pressure ratio h as possible, and to meet h' < h;
the jet pump actual pressure ratio h' is expressed as:
Pjetpumb＝ρliftgH+hlift+hv
Wherein: p jetpumb is the energy required by the ore pulp to be lifted to the ground without back pressure, and the unit Pa; ρ lift is the flow path pulp density in the double-wall drill pipe, unit kg/m 3; g is gravity acceleration, and m/s 2;hlift is the on-way resistance of the pulp in the flow path of the double-wall drill pipe, and the unit is Pa; h int is the along-the-way resistance of the double-wall drill rod outer flow channel water inlet pipe, and the unit is Pa; h v is the dynamic pressure of the pulp in the flow path in the double-wall drill pipe, and the unit Pa; h is the lifting height of ore pulp, and the unit is m; p b is hydraulic mining back pressure, unit Pa; p pumb is the pressure of high-pressure water, in Pa;
The slurry density ρ lift of the double-wall drill pipe inner flow path in the formula of the energy P jetpumb required for lifting the slurry to the ground under the condition of no back pressure is expressed as follows:
Wherein: ρ p is the mineral seam density in kg/m 3; ρ is the high-pressure water density, the unit kg/m 3;Qwater is the liquid flow rate in the sucked fluid in the slag returning pipe, the unit m 3/s;Qcoal is the particle flow rate in the sucked fluid in the slag returning pipe, the unit m 3/s;Q'0 is the working fluid flow rate of the jet pump in the fluidization mining process, the unit m 3/s;Q's is the sucked fluid flow rate of the jet pump in the fluidization mining process, and the unit m 3/s;
the dynamic pressure h v of the pulp in the flow path in the double-wall drill pipe in the formula of the energy P jetpumb required for lifting the pulp to the ground under the condition of no back pressure is expressed as follows:
Wherein: u lift is the flow rate of pulp in the flow path of the double-wall drill pipe, and the unit is m/s; a inner is the inner diameter of the double-wall drill rod, and the unit is m;
The energy P jetpumb formula required by lifting the ore pulp to the ground under the condition of no back pressure and the actual pressure ratio h' formula of the jet pump are expressed as the along-path resistance h lift of the ore pulp in the double-wall drill pipe inner flow passage and the along-path resistance h int of the water inlet pipe of the double-wall drill pipe outer flow passage:
Wherein: lambda lift is the friction coefficient of the inner flow passage of the double-wall drill rod, and 0.04 is taken; d lift is the hydraulic diameter of the flow path in the double-wall drill rod, and the unit is m; lambda int is the friction coefficient of the outer flow passage of the double-wall drill rod, and 0.04 is taken; d int is the hydraulic diameter of the outer flow channel of the double-wall drill rod, and the unit is m; u int is the speed of the outer flow channel of the double-wall drill rod, and the unit is m/s;
Step2-2, adjusting the outlet diameter D jet of the hydraulic cutting nozzle and the outlet diameter D subjet of the turbulent nozzle so that the actual flow ratio q 'of the jet pump in the fluidization mining process is as close as possible to the theoretical flow ratio q of the jet pump, and q' < q is satisfied;
the actual flow ratio q' of the jet pump is expressed as:
wherein: q' 0 is the jet pump working fluid flow; q' s is the flow rate of the fluid absorbed by the jet pump;
the jet pump working fluid flow rate Q '0 and the jet pump suction fluid flow rate Q' s are represented as:
Q's＝Qwater+Qcoal
Wherein: u is the high-pressure water speed, and the unit is m/s; d 1 is the nozzle outlet diameter, in m; q water is the flow rate of liquid in the sucked fluid in the slag returning pipe, the unit m 3/s;Qcoal is the flow rate of particles in the sucked fluid in the slag returning pipe, the unit m 3/s;λjet is the flow rate coefficient of the nozzle, and the flow rate coefficient is 0.975; d jet is the diameter of the outlet of the hydraulic cutting nozzle, and the unit is m; d subjet is the outlet diameter of the turbulent nozzle, and the unit is m; p pumb is the pressure of high-pressure water, in Pa; ρ is the high pressure water density in kg/m 3; g is the gravitational acceleration, unit m/s 2; h is the lifting height of ore pulp, and the unit is m; p b is hydraulic mining back pressure, unit Pa; h int is the along-the-way resistance of the double-wall drill rod outer flow channel water inlet pipe, and the unit is Pa;
Step3, verifying process matching degree: the cavitation flow ratio q k is the maximum flow ratio that the jet pump does not generate cavitation under the premise of the given jet pump structure size, whether the actual flow ratio q 'of the jet pump in the fluidization mining process is smaller than the cavitation flow ratio q k is verified, and if the actual flow ratio q' is smaller than the cavitation flow ratio q k, the jet pump structure size obtained by Step1 and the fluidization mining process parameter obtained by Step2 are the best matched parameters; if not, modifying the initial value of the jet pump area ratio m or the flow ratio q according to the empirical value, and repeating the steps Step1 to Step3 until the actual flow ratio q' of the jet pump in the fluidization mining process is smaller than the cavitation flow ratio q k.
2. The method for designing parameters of a drilling non-submerged jet fluidization mining process according to claim 1, wherein in Step1, when the fluid to be sucked is a liquid-solid system, a basic equation of the jet pump is as follows:
Wherein: Is the flow velocity coefficient of the nozzle; /(I) Is the flow velocity coefficient of the throat; /(I)Is the flow velocity coefficient of the diffusion tube; /(I)Taking 0.95 for the flow velocity coefficient of the suction chamber; /(I)Taking 1 as a flow velocity coefficient of an inlet section of the throat pipe;
Mu 1 is the correction coefficient of the particle and liquid velocity slip of the outlet section of the suction chamber; mu 2 is the correction coefficient of the particle and liquid velocity slip of the throat inlet section; mu 3 is the correction coefficient of the particle and the liquid velocity slip of the throat outlet section;
a is a throat inlet function; c is the suction area ratio; q is the theoretical flow ratio; m is the area ratio; n is a coefficient related to the area ratio; delta is the fluid momentum correction coefficient of the throat outlet section; beta is the contraction half angle of the inlet section of the throat;
f 3 is the throat inlet area, unit m 2;f1 is the nozzle outlet area, unit m 2;fs1 is the flow area of the sucked fluid in the section of the suction chamber outlet, and unit m 2;
k 1 is the non-uniform coefficient of the flow velocity distribution of the working fluid at the inlet section of the throat, and 0.95 is taken; k' 1 is the non-uniform comprehensive coefficient of the flow velocity distribution of the working fluid at the inlet section of the throat; k 2 is the non-uniform coefficient of the flow velocity distribution of the sucked fluid at the inlet section of the throat, and 1.10 is taken; k' 2 is the non-uniform comprehensive coefficient of the flow velocity distribution of the working fluid at the inlet section of the throat; is the volume-weight ratio of the absorbed fluid to the working fluid.
3. A method of designing parameters of a drilling non-submerged jet fluidization mining process according to claim 2, wherein the correction coefficient μ 1 of the suction chamber outlet profile particle and liquid velocity slip is expressed as:
Wherein: c v is the particle volume concentration; the average flow velocity of the solid particles in the outlet section of the suction chamber is expressed in m/s; v s1 is the average flow velocity of the sucked fluid at the outlet section of the suction chamber under the influence of neglecting particles, and the unit is m/s; q s is the flow rate of the sucked fluid of the jet pump, the unit m 3/s;fs1 is the flow area of the sucked fluid in the section of the outlet of the suction chamber, the unit m 2;D1 is the diameter of the outlet of the nozzle of the jet pump, and the unit m; l c is the throat distance, unit m; m is the area ratio; beta is the contraction half angle of the inlet section of the throat; v ss is the fluid flow rate at the suction port, in m/s; f drags is the drag force exerted by the slurry suction port particles, and the unit is N; g is the gravitational acceleration, unit m/s 2; a is the projection area of particles along the water flow direction, the unit m 2;a1 is the nozzle wall thickness correction coefficient, and 1.2 is taken; d p is the maximum particle diameter of particles at the slurry suction port, and the unit is m; gamma p particle volume weight, unit N/m 3;γs is fluid volume weight of the pulp suction port, unit N/m 3;Vp is volume of the maximum particle size particle at the pulp suction port, and unit m 3; /(I) The sedimentation end speed of the particles with the maximum particle size at the pulp suction port is in m/s; s is the area of a suction inlet, and the unit m 2;Ls is the length of a suction chamber and the unit m; c d is the drag coefficient of the particles, and 0.44 is taken;
The correction coefficient mu 2 of the throat inlet profile particle and the liquid velocity slip is expressed as:
Wherein: v s2 is the average flow velocity of the sucked fluid in the section of the throat inlet under the influence of neglecting particles, and the unit is m/s; The average flow velocity of the solid particles at the inlet section of the throat pipe is in units of m/s; f drag1 is the drag force exerted by the solid particles in the outlet section of the suction chamber, unit N; f 3 is the throat inlet area, unit m 2;f1 is the nozzle outlet area, unit m 2;γ1 is the volume weight of the fluid at the inlet section of the throat, and unit N/m 3;
The correction coefficient mu 3 of the throat outlet profile particle and the liquid velocity slip is expressed as:
Wherein: q is the theoretical flow ratio; v s3 is the average flow velocity of the fluid at the throat outlet section under the influence of neglected particles, in m/s; The average flow velocity of the solid particles at the section of the outlet of the throat pipe is expressed in m/s; f drag2 is the drag force exerted by the solid particles on the inlet section of the throat pipe, and the unit is N; gamma 2 is the volume weight of the fluid at the inlet of the throat, the unit N/m 3;Q0 is the flow rate of the working fluid of the jet pump, and the unit m 3/s;Lt is the length of the throat.
4. A method of designing parameters of a drilling non-submerged jet fluidization mining process according to claim 1, wherein in Step3, the cavitation flow ratio q k is expressed as:
Wherein: m is the area ratio of the jet pump; h k is cavitation pressure ratio; epsilon is the cavitation flow ratio coefficient;
Cavitation pressure ratio h k is expressed as:
Wherein: p a is the atmospheric pressure, unit Pa; p b is hydraulic mining back pressure, unit Pa; p pumb is the pressure of high-pressure water, in Pa; ρ lift is the flow path pulp density in the double-wall drill pipe, unit kg/m 3; g is the gravitational acceleration, unit m/s 2; h is the lifting height of ore pulp, and the unit is m; h int is the along-the-way resistance of the double-wall drill rod outer flow channel water inlet pipe, and the unit is Pa; p k is the saturated vapor pressure of water in Pa.
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Citations (9)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| CN201050511Y (en) * | 2007-06-06 | 2008-04-23 | 中电投远达环保工程有限公司 | Jet pump applied in wet desulfurization forced oxidation |
| CN102797465A (en) * | 2012-09-10 | 2012-11-28 | 河南理工大学 | Underground ultra-thin virtual protection layer hydraulic coal mining method |
| CN204458567U (en) * | 2015-01-28 | 2015-07-08 | 中国海洋石油总公司 | Adjustable jet pump |
| CN110360165A (en) * | 2019-07-02 | 2019-10-22 | 江苏瑞洪盐业有限公司 | A kind of twin-stage jet pump design method and device |
| CN110685964A (en) * | 2019-11-13 | 2020-01-14 | 四川大学 | Jet pump capable of automatically and uniformly supplementing air and reducing corrosion |
| RU2732615C1 (en) * | 2019-09-06 | 2020-09-21 | Общество С Ограниченной Ответственностью "Марс" | Method of well operation by jet pump and installation for implementation thereof |
| CN113536507A (en) * | 2021-07-28 | 2021-10-22 | 南京工业职业技术大学 | Jet pump design method based on theoretical model and CFD correction |
| CN216142984U (en) * | 2021-07-01 | 2022-03-29 | 中国航空工业集团公司沈阳飞机设计研究所 | Jet pump |
| CN114718458A (en) * | 2022-04-01 | 2022-07-08 | 中国石油大学(华东) | Drilling device without riser gas lift and pump lift combined lifting and parameter design method thereof |
Family Cites Families (2)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| US20050121191A1 (en) * | 2003-12-08 | 2005-06-09 | Lambert Mitchell D. | Downhole oilfield erosion protection of a jet pump throat by operating the jet pump in cavitation mode |
| EP2602451B1 (en) * | 2010-08-04 | 2017-03-01 | Toyota Jidosha Kabushiki Kaisha | Control device for internal combustion engine |
-
2022
- 2022-09-26 CN CN202211173194.6A patent/CN115422684B/en active Active
Patent Citations (9)
| Publication number | Priority date | Publication date | Assignee | Title |
|---|---|---|---|---|
| CN201050511Y (en) * | 2007-06-06 | 2008-04-23 | 中电投远达环保工程有限公司 | Jet pump applied in wet desulfurization forced oxidation |
| CN102797465A (en) * | 2012-09-10 | 2012-11-28 | 河南理工大学 | Underground ultra-thin virtual protection layer hydraulic coal mining method |
| CN204458567U (en) * | 2015-01-28 | 2015-07-08 | 中国海洋石油总公司 | Adjustable jet pump |
| CN110360165A (en) * | 2019-07-02 | 2019-10-22 | 江苏瑞洪盐业有限公司 | A kind of twin-stage jet pump design method and device |
| RU2732615C1 (en) * | 2019-09-06 | 2020-09-21 | Общество С Ограниченной Ответственностью "Марс" | Method of well operation by jet pump and installation for implementation thereof |
| CN110685964A (en) * | 2019-11-13 | 2020-01-14 | 四川大学 | Jet pump capable of automatically and uniformly supplementing air and reducing corrosion |
| CN216142984U (en) * | 2021-07-01 | 2022-03-29 | 中国航空工业集团公司沈阳飞机设计研究所 | Jet pump |
| CN113536507A (en) * | 2021-07-28 | 2021-10-22 | 南京工业职业技术大学 | Jet pump design method based on theoretical model and CFD correction |
| CN114718458A (en) * | 2022-04-01 | 2022-07-08 | 中国石油大学(华东) | Drilling device without riser gas lift and pump lift combined lifting and parameter design method thereof |
Non-Patent Citations (4)
| Title |
|---|
| Shaojun Liu等.Influence of the Blade Angle of Guide Vane Outlet on the Performance of Lifting Electric Pump in Deep Sea Mining.2019 International Conference on Intelligent Transportation, Big Data & Smart City (ICITBS).2019,全文. * |
| 夏柏如;曾细平;毛志新.一种钻孔水力采煤系统的研究.地学前缘.2008,(04),全文. * |
| 綦耀光;刘冰;张芬娜;刁秀芳;莫日和;尚晓林;黄芳宇.煤层气井负压射流快速排煤粉装置研究.中国矿业大学学报.2014,(01),全文. * |
| 邓金先;石雨冬;庄会涛;刘冰;徐兴平.新型双喷嘴射流泵水力特性的试验研究.石油机械.2017,(02),全文. * |
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