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Mecânica das Rochas para Recursos Naturais e Infraestrutura SBMR 2014 – Conferência Especializada ISRM 09-13 Setembro 2014 © CBMR/ABMS e ISRM, 2014 SBMR 2014 Hoek & Brown and Barton & Bandis Criteria Applied to a Planar Sliding at a Dolomite Mine in Gandarela Synclinal Felipe Giusepone Vale do Rio Doce Company, Belo Horizonte, Brazil, Email: Felipe_g07@hotmail.com Prof. Dr. Lineu Azuaga Ayres da Silva Escola Politécnica da Universidade de São Paulo, São Paulo, Brazil, Email: layres@usp.br SUMMARY: It was utilized the Hoek & Brown, (1997) rupture criterion (as presented in the version of 2000 by Marinos and Hoek ) and the criterion of Barton & Bandis (1982) for the study of the slope stability in a Dolomite open pit mine situated in the Gandarela synclinal. The results obtained with these criteria were evaluated to verify the compatibility between the two methods. KEYWORDS: Empirical Design Methods; Hoek & Brown; Barton & Bandis; plane failure; Slope Engineering; open pit mines; dolomite 1 INTRODUCTION For the case study was used the Dolomite mine situated in Gandarela Synclinal due to the plane sliding problems that occurred very frequently in the North open pit region. The facility to obtain the necessary data for empirical studies was very important for the employment of these methods. 2 UTILIZATION 2.1 Regional Geology The area is located in the “Quadrilátero Ferrífero”, a very important region of iron mining in the center of Minas Gerais state. According to Dorr (1969) the stratigraphic column of the “Quadrilátero” is composed of: the Basement consisted of gneiss, amphibolites, metaultramafics and pegmatites; Super Groups “Rio das Velhas”: volcano-sedimentary sequence of the type greenstone belt; and the Super Group Minas: metasedimentary rocks with small volcanic rocks contributions consisted of quartzite, phyllite, metaconglomerates, iron formations and limestones. The Gandarela Formation belongs to the Itabira Group and the Super Group Minas. It was identified by Dorr (1969) in the homonymous Synclinal at East of the “Quadrilátero Ferrífero”. This Formation is constituted of dolomites, limestones, dolomitic phyllites, iron dolomitic formations, phyllites and quartzous lenses. The most important lithology for the analysis of plane sliding study is the Impure Dolomite (DI) that is a constituent of the mine base strata. 2.2 Kinematic Analysis of Rupture It was used the method of Markland (1972) to identify the open pit regions with highest plane instability potential. The collection of the structural discontinuities attitudes presents in the rock mass was located in the field together with the proposed final geometry of the open pit mine. Four families of discontinuities were identified with the following attitudes: Stratification: attitude 244N/S26E/36SE; Family 1: attitude 237N/S32E/82SE; Family 2: attitude 120N/N30E/54NE; Family 3: attitude 94N/N2E/46NE. Eighty field measurements were carried out and the above values are averages of the measures for each family of discontinuity. The possibility of plane rupture has been identified in North slope of the open pit as shown in Figure 1. SBMR 2014 The discontinuity involved in analysis of rupture is the bedding layer (foliation) and lithology DI that remains in the mining final configuration. Figure 1. Kinematic analysis of the possibility of breakage in the dolomite configuration of open pit mine 2.3 HOEK & BROWN criterion (1997) adapted by Marinos and Hoek (2000) This criterion is based on the classification "Geological Strength Index" (GSI) to determine the estimated strength of rock mass. The GSI is determined by abacus (attachment 1) developed by Marinos and Hoek (2000) and depends on the characteristics of discontinuities and rock mass structure. These characteristics were determined through geomechanics description of drill holes and the calculation of "Rock Quality Designation (RQD) used to assess the degree of rock mass natural fracturing and guide to obtaining factor GSI on 60 points. This value was obtained by considering the structure of the rock very blocky and with regular quality of surface discontinuity in accordance with the abacus (attachment 1). The parameter mi is obtained according to the origin of the rock and determined through by the table (attachment 2). This parameter was regarded as 9 ± 3 due to the sedimentary formation and texture very thin. By means of laboratory testing conducted at Escola Politécnica da Universidade de São Paulo was determined the uniaxial compressive strength of rock core samples for DI of 147.80 MPa. The rock mass strength is estimated by means of equations 1 to 3 which consider the scaling factor to correct the lab results. The modeling below considers the condition of unweathered rock and GSI > 25. (1) For GSI = 60, we have S = 0.0117 (2) For mi = 9, we have mb = 2.1569 Therefore the equation obtained for the rock mass using the GSI is: (3) By varying the value of σ3 it is possible to determine the shear envelope which characterizes the rock mass behavior in the presence of requesting efforts, as Figure 2 demonstrates. Figure 2. Rock mass shear envelope obtained by the equation GSI Therefore, the equation of rupture envelope is obtained as described in equation (4) (4) 2.3.1 Plane Sliding Analysis The Figure 3 presents the required geometry for the plane rupture in the North slope. δ σ n 9 100GSI eS 28 100 . GSI ib emm 5.0 3 31 0117.0 80.147 1569.2.80.147 x 30tan38.11 n SBMR 2014 Figure 3. Chart for plane rupture analysis The safety factor obtained through the Hoek and Bray methodology (1981) is calculated by means of equation 5. (5) Where: Ψp= Dip angle of the sliding plane (°); c = cohesion in the rupture surface (Mpa); = angle of friction (°); A = surface length (m); U = Resultant force of water pressure on the plane of discontinuity (tf/m); V = Resultant force of water pressure on tension crack (tf/m); W = Potentially unstable block weight (tf/m). According to the equations 6 to 9 one can calculate: (6) (7) (8) (9) The obtained values are: A = 187.14 m W = 6,303.13 tf/m; U = 2,392.46 tf/m; V = zero (without crack tension) It was also considered the contribution of the weight of coverage (soil) on the surface of rupture using the equation 10.(10) The achieved value was 1,206.98 tf/m that adding to the weight of the potentially unstable rock block results in the weight of 7,510.13 tf/m. Therefore, at the angle of 45° (angle provided by the final configuration of the proposed open pit), the F.S. of 0.96 was obtained, considered unstable and outside the safety margin (F.S. ≈ 1.25). General angle alternatives for this face were simulated, the obtained data are presented in Table 1. Table 1. Simulations results for calculus of F.S. and slope general angle for the open pit North region. Ψf (o) Cohesion (MPa) A (m) W (tf/m) U (MPa) Θ (o) F.S. 38 11.38 187.14 1,560.46 2,392.46 30 1 1,61 40 11.38 187.14 3,145.07 2,392.46 30 1,20 42 11.38 187.14 4,725.65 2,392.46 30 1,06 45 11.38 187.14 7,510.12 2,392.46 30 0,96 50 11.38 187.14 10,449.74 2,392.46 30 0,92 65 11.38 187.14 17,998.24 2,392.46 30 0,87 Evaluating table 1 one can verify that the angle of 38° to 40° is the best option for the open pit general angle in the North slope according to the methodology of Hoek and Brown (1997). 2.4 BARTON & BANDIS Criterion (1982) This criterion was developed for the exclusive study of the plane sliding analysis and correlates the uniaxial compressive rock strength (drill hole) with the rock mass uniaxial compressive strength by means of "tilt tests" and sclerometer Schmidt. As well as the GSI is important to determine the characteristics of the discontinuities of the Rock slope plane Soil slope plane Descontinuit y bedding plane pp pp VsenW senVUWcA SF cos.. tan..cos. .. peczHA cos. pWW ecHU cos... 4 1 2 2 .. 2 1 ww zV 1cot.cot.cot.1... 2 1 22 fppH zHW csss HW cot... 2 1 2 SBMR 2014 studied rock mass, the Barton and Bandis criterion (1982) uses the compressive surface strength obtained by means of the Schmidt sclerometer to determine these characteristics using the JCS parameter (coefficient of superficial compressive strength) and the JRC (coefficient of the discontinuities roughness). The JCS is obtained directly from the sclerometer test performed on a cut surface (sawn). It was considered JCS = 66.14 MPa. The JCR is calculated by the equation 11. (11) The residual friction angle (Φr) is obtained by means of the equation 12. (12) The angle (Φ bbb) is the angle of friction between two surfaces cut (sawn), as Figure 4 illustrates the "Tilt Test." It was considered Φ bbb = 32˚. The correction parameter (r/R) is obtained by calculating the ratio between the superficial compressive strengths on the weathered discontinuity (r) on the sawn surface (R). This parameter was estimated at 1.0313. Figure 4. Representation of the "Tilt Test." So according to the equation (12) Φr = 32.63˚, the difference between α – Φr can be characterized as the increment in friction angle arising from "asperity" of the discontinuity surface. This value was estimated by means of the experiment of "Tilt Test" subtracting values between natural and sawn surfaces (cut). It was considered i = α – Φr = 8°. The normal stress (σns) is determined by means of the weight of the tested sample ("Tilt Test") and the contact surface between these samples. The σns value was estimated at 0.0036 MPa. Finally using the equation 11, one has JRC = 9.52 MPa. Barton and Bandis (1982) correct the values obtained in the laboratory to get the interested field values using the scaling factor based on the relationship between the length of the tested samples (14.5cm) and the length of the discontinuity susceptible to plane sliding in the field (187.14m). The parameters JRC and JCS are corrected employing the equations 13 and 14. (13) (14) Thus: JRC = 78.56 MPa and JCS = 250.57 MPa. 2.4.1 Plane sliding Analysis Figure 3 shows the required geometry for the plane sliding in the North slope. The safety factor obtained by means of Barton and Bandis criterion (1982) is calculated using equation 15. (15) The weight of the rock block (W) and the uniaxial compression strength (σ) are the same as considered by the criterion of Hoek & Brown. So for the angle of 44° it was obtained the F.S. of 1.26. ns r JCS JRC 10log R r br .2020 003.0 0 0. JRC n L L JCSJCS senW JCS JRCW SF r n . log.tan.cos. .. 10 002.0 0 0. JRC n L L JRCJRC SBMR 2014 3 RESULTS The criteria of Hoek & Brown (1997) adapted by Marinos & Hoek (2000) and Barton & Bandis (1982) showed consistency for the analysis of plane sliding. The figure 5 presents the values obtained using these two criteria. Figure 5. Relation of FS obtained using the criteria of Hoek-Brown (1997) and Barton and Bandis (1982). The probable stability of this slope occurs between the angles of 38° to 40° and 42° to 44° according to the criteria of Hoek & Brown and Barton & Bandis respectively for F.S. around 1.25. This difference of 2° to 4° can be considered insignificant in the field and of difficult verification in large mineral slopes. The two criteria determined the angle of 50° as the limit value for stability (F.S. = 1.0). Considering the project angles occur significant differences between the methodologies of analysis, such as: the angle of 40° presents F.S. = 1.45 in accordance with the criterion of Barton and Bandis and F.S. = 1.20 according to Hoek and Brown. There is a difference of 21%. 4 CONCLUSION According to Hoek and Brown (1997) the methodology GSI should not be used in rock masses where the problems of instabilities are caused by planes bedding. The ISRM recommends the use of the criterion of Barton and Bandis (1982) in these cases. This article raise the possibility of further studies to confirm the recommendation of the ISRM and the possibility to assert compatibility between these methods. This compatibility should be tested and confirmed in research and future studies. REFERENCES Barton, N; Bandis, S. Effect of block size on the shear behavior of jointed rock [Keynote lecture]. In: U.S. SYMPOSIUM ON ROCK MECHANICS, 23rd., 1982, Berkeley, Cal. Proceedings. New York: Soc of Min Eng of AIME, 1982. p. 739-760. Dorr, J.V.N. Physiographic, stratigraphic and structural development of the quadrilátero ferrífero, Minas Gerais, Brazil. Washington, D.C., 1969. 110 p. (U.S. Geological Survey Professional Paper, 641-A). Hoek, E.; Bray J. Rock slope engineering. London: The Institution of Mining and Metallurgy, 1981. 358 p. Hoek, E.; Brown, E.T. Practical estimates of rock mass strength. Intnl. J. Rock Mech.& Mining Sci. & Geomechanics Abstracts. 1997. p.1165-1186. Marinos, P.; Hoek, E. GSI: a geologically friendly tool for rock mass strength estimation. In: INTERNATIONAL CONFERENCE ON GEOTECHNICAL & GEOLOGICAL ENGINEERING, 2000, Melbourne. GeoEng2000. Lancaster: Technomic, 2000. p. 1422- 1489. Markland, J.T. A useful technique for estimating the stability of rock slopes when the rigid wedge sliding type of failure is expected. London: Imperial College, 1972. 10 p. (Imperial College Rock Mechanics Research Report, n. 19). 0 0.2 0.4 0.6 0.8 1 1.2 1.4 1.6 1.8 38 40 42 45 50 60 65 Slope plane angle Security factor (F.S) Barton_Bandis Hoek _Brown SBMR 2014 Attachment 1. Abacus to Obtain the Dolomite GSI, Reference: Marinos and Hoek (2000) Attachment 2. Values Of The Constant mi for Intact Rock, by Rock Group 4 . Reference: Marinos And Hoek (2000)
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