We proposed a poly-dimethylsiloxane (PDMS)-coated fiber Bragg grating (FBG) temperature sensor for enhancing temperature sensitivity. By embedding the bare FBG in a temperature-sensitive elastomeric polymer, the temperature sensitivity of the proposed structure could be effectively improved by 4.2 times higher than those of the conventional bare-type FBG sensors due to the high thermal expansion coefficient of the PDMS. We analyzed the temperature-sensitivity enhancement effect with the increased Bragg wavelength shift in our structure and dependence on the temperature sensitivity with respect to the cross-section area of the PDMS. In the past decades, fiber Bragg grating (FBG) sensors have been studied extensively for sensing several types of physical parameters such as temperature, strain, bending, and pressure [1 - 6] with optical methods. FBG sensors have the advantages of immunity to electromagnetic interference, compact structure, simple fabrication, and easy construction of long range monitoring system by using wavelength-multiplexing schemes with cascaded FBGs. However, for temperature sensing itself, the temperature sensitivities of bare FBG sensors are low due to the low thermal expansion coefficient of silica with temperature variation [1] . To increase the temperature sensitivity of the FBG sensor, several types of modified FBG sensors have been proposed. The earlier researchers studied deposition methods using metal or metal complex compounds with high thermal expansion coefficients to enhance the temperature sensitivity [7 - 10] . However, the metal deposition process on the silica fiber requires complex fabrication steps, for which it is difficult to control the deposition layer precisely due to the radial shape of optical fibers. The residual stress, produced during the metal deposition process, on the interface between the deposited metal and the glass also makes it difficult to design the resonant peaks of the metal-deposited FBG sensors precisely [10] . For the case of using polymers for enhancing the tem-perature sensitivity of FBG sensors, the fabrication process can be comparatively simple because the polymer cladding layer can be made simply by a general coating process, but their temperature sensitivities are not good due to the low thermal expansion coefficient [11 , 12] . In addition, the thermal dimensional stability of a polymer should be con-sidered to be used for the temperature-sensitivity-enhancing materials because the thermally expanded volume of most polymers cannot be restored completely to an initial volume after cooling. In this study, we propose a poly-dimethylsiloxane (PDMS)- coated FBG temperature sensor, where the PDMS is used for enhancing temperature sensitivity as shown in Fig. 1 . The thermal expansion coefficient of the PDMS is much higher than those of metal materials previously used for enhancing temperature sensitivity in metal-coated FBG sensors as shown in Table 1 [13 , 14] . Thus, the temperature sen-sitivity can be effectively enhanced by the tensile force induced by the thermally expanded PDMS. Because the PDMS is a chemically stable elastomeric polymer, the thermally shifted resonant peak in our structure moves back to an initial wavelength without dimensional stability problems. In addition, we can make the PDMS jacket on the FBG very easily due to its good adhesion on the silica surface by using a simple molding process [15] . However, the enhancement of the temperature sensitivity in the PDMS-coated FBG sensor is not much higher than the large thermal expansion coefficient of the PDMS itself. It is because the Young’s modulus of the silica is much higher than that of the elastomeric PDMS. Here, we give an analytic model to describe the enhanced Bragg wavelength shift of the proposed structure in response to the increased temperature, and we demonstrate the temperature sensitivity according to cross-section areas of the PDMS jackets. The FBG structure can measure the temperature variation by monitoring the shift (Δ λ_B ) in the Bragg resonance wave-length( λ_B ) induced by surrounding temperature variation. When temperature is varied, λ_B is shifted to longer or shorter wavelength due to the thermally varied effective refractive index of the fiber and the thermally varied Bragg grating periodicity. In our PDMS-coated FBG temperature sensor, the λ_B is additionally shifted by the tensile force of the thermally expanded PDMS jacket. Considering the reciprocal force ( F_r ) equally applied to the optical fiber and the PDMS jacket in our PDMS-coated FBG sensor, the tensile forces onto the fiber ( F_tf ) and onto the PDMS jacket ( F_tp ) can be expressed as follows. where F_f and F_p are the thermally induced tensile forces applied onto the fiber and PDMS jacket, respectively, when it is assumed that there is no force interaction between the optical fiber and the PDMS jacket at the interface. Thus, both F_f and F_p can be obtained with the material para-meters of the thermal expansion coefficients. Since the thermally induced length variation (Δ L ) is the same at the fiber and the PDMS jacket in our PDMS-coated FBG sensor, Δ L can be expressed by modification of Eq. (1) as follows. where k_f and k_p are the elastic constants of the bare fiber and the PDMS, respectively. Δ L_f and ΔL_p are the thermally induced length variation of the fiber and the PDMS, respec-tively, assuming that there is no interaction force between the fiber and the PDMS. Δ L^r _f and Δ L^r _p are the additional length variation of the fiber and the PDMS, respectively, induced by the reciprocal force in the PDMS-coated FBG structure. Considering that the thermal expansion coefficient of the PDMS is much higher than that of the silica fiber, we can see that the thermal expansion of the PDMS is restricted by the amount of Δ L^r _p , whereas the thermal expansion of the FBG is enhanced by Δ L^r _f . Since F_r can be written from Eqs. (1) and (2) by where Δ L can be expressed after some calculations by using the Young’s modulus equation [16] as follows. Here, A_p and A_f denote the cross-section area of the PDMS and the optical fiber, respectively, in our PDMS-coated FBG structure. E_p and E_f are the Young’s modulus values of the PDMS and the silica fiber, respectively. Equation (4) shows that the thermally induced length variation in our PDMS-coated FBG structure can be expressed by the device dimen-sion parameters and the material parameters of the thermal expansion coefficients. Considering the thermally induced refractive index variation in the silica fiber, the Bragg wavelength shift of the PDMS-coated FBG sensor according to temperature change can be written as follows. where α_n , α _f , α_p , and Δ T are the thermo-optic coefficient (~8.6×10 ^-6 ℃) of the silica fiber, the thermal expansion coefficient (~0.55×10 ^-6 m/m℃) of the fiber, the thermal expansion coefficient (~300×10 ^-6 m/m℃) of the PDMS, and the temperature variation amount, respectively [13 , 17] . Since Δ L_f and Δ L_p in Eq. (4) are written by Δ L_f = L Δ Tα _f and ΔLp = LΔTα_p , respectively, Δλ_B is finally derived from Eqs. (4) and (5) as follows, where is the effective photoelastic coefficient (~0.212) of the fiber [17] . For the PDMS-coated FBG sensor, the FBG (SMF-28) with total longitudinal grating length of 10 mm was utilized in our experiments, which presented the central wavelength of 1549.6 nm, the 3 dB bandwidths of about 0.1 nm and 0.2 nm, and the peak reflectivity of about 90%. Before coating the PDMS onto the FBG, the cladding surface of the FBG was pretreated with the oxygen plasma at 30 W for 30 seconds to enhance the interfacial adhesion between the PDMS and the optical bare fiber [18] . The PDMS jacket was fabricated with a molding process by using the PDMS with a 10:1 mixing ratio of precursor of elastic material (Sylgard 184-A) and hardener (Sylgard 184-B), where the length of the PDMS jacket was L =70 mm. The FBG was precisely aligned to be positioned at the center of the PDMS block. In the mold, the prepolymer of the mixtures was polymerized by baking at 60℃ for 12 hours. Finally, the PDMS-coated FBG sensors were completed by removing the mold. Three kinds of the PDMS-coated FBG sensors with the different cross-section areas ( A_p =5×5 mm ² , A_p =10×10 mm ² , A_p =20×20 mm ² ) of the PDMS jackets were prepared to check the temperature sensitivity depending on the device dimension condition of the PDMS jacket and to compare the experimental results with the derived analytic model. For the PDMS-coated FBG sensor with the PDMS jacket with A_p =5× 5 mm ² , the bare FBG with the 3 dB bandwidth of 0.1 nm was used. For the others, the 3 dB bandwidth of the bare FBG was 0.2 nm. As shown in Fig. 2 , a broadband light source (Opto-Link Corporation Ltd. OLS15CLGB-15FA) was connected to the proposed FBG sensor with an optical isolator. The trans-mission spectra of the PDMS-coated FBG sensor were monitored using an optical spectrum analyzer (OSA, Ando AQ-6315A) with a resolution bandwidth of 0.05 nm. During the experiments, temperature was precisely controlled from 30℃ to 120℃ by using a temperature-controlled pyrostat. Figure 3 shows the transmission spectra of the PDMS-coated FBG sensors at various temperatures, where the cross-section areas of the PDMS-jackets are A_p =5×5 mm ² , A_p =10×10 mm ² , and A_p =20×20 mm ² . In all cases, the measured Δλ _B 's increase with increasing temperature due to the thermal expansion effect of the PDMS jackets as we can see from Eq. (6). Figure 3 shows that the shapes as well as the 3 dB bandwidths of the thermally shifted transmission spectra are the same during the temperature sweep which means that the tensile force induced by the PDMS jacket is uni-form without producing additional bending distortions. In addition, the thermally shifted Bragg wavelengths are moved back to the initial λB after cooling to initial temperature irrespective of the tensile stress amount induced by the thermally expanded PDMS jacket within our experiment con-ditions,which shows that the adhesion between the silica cladding surface and the PDMS jacket is good and, due to its good elasticity, there is no dimensional stability problem or residual stress problem in our PDMS jacket Figure 4 (a) shows ΔλB|s of the PDMS-coated FBG sensors for various cross-section areas of the PDMS jacket according to temperature variation, where the dots and the lines denote the experimental results and the simulation results from Eq. (6). For comparison, Δλ _B' s of the bare FBG without the PDMS jacket are plotted together. In all cases, Δλ _B increases linearly with increasing Δ T as expected from Eq.(6). However, the temperature sensitivity of the bare FBG was 0.010 nm/℃ . On the other hand, the temperature sensiti-vities of the PDMS-coated FBG sensors were much higher than that of the bare FBG. They were enhanced to 0.026 nm/℃ (for A_p = 25 mm ² ), 0.033 nm/℃ (for A_p = 100 mm ² ), and 0.042 nm/℃ (for A_p = 400 mm ² ). Equations (4) and(6) show that the tensile force thermally induced by the PDMS jacket can be effectively delivered to the inner FBG with increasing A_p . Thus, the temperature sensitivity increases with increasing A_p of the PDMS-coated FBG sensor. The temperature sensitivity of the PDMS-coated FBG sensor is comparable to that (~0.048 nm/℃ ) of the metal-coated FBG temperature sensor [10] . However, the PDMS-coated FBG sensor can be made by the simple molding process without any residual stress problem during fabrication compared to conventional metal-coated FBG sensors so that the initial resonance wavelength as well as the amount of the temperature-induced resonant wavelength shift can be precisely designed. The material parameters used for theoretic values, as depicted in Fig. 4 , from Eq. (6) are that the diameter of the bare fiber is 125 ㎛ , and the Young’s moduli of the PDMS and the bare fiber are E_p =750 Kpa and E_f =72 Gpa, respec-tively [19 , 20] . For the thermal expansion coefficient of the PDMS, the fitted value ( α_p =312 × 10 ^-6 m/m?℃) from the experimental results was used. It was slightly higher than that from the data sheet shown in Table 1 . The thermal expansion coefficient of PDMS varies slightly depending on the mixing ratio of the prepolymers and the irregularly entangled polymer chain network structure [21] . For the PDMS-coated FBG sensors with the PDMS jacket conditions of A_p = 100 mm ² and A_p = 400 mm ² , the simulation results of Δλ _B with Eq. (6) and the same material conditions matched well with the experimental results. However, for the case of A_p = 25 mm ² , the analytic results agreed with the experi-mental results when A_p = 49 mm ² was used for the cross-section area of the PDMS-jacket at the same material con-ditions.The difference might originate in our molding process. Figure 4 (b) shows the temperature sensitivity of the PDMS-coated FBG sensor for various values of A_p , which was plotted with Eq. (6). For comparison, the experimental values obtained with Fig. 4 (a) were plotted together. Figure 4 (b)shows that the temperature sensitivity enhancement effect by the PDMS jacket is high with increasing A_p at small values of A_p . However, the enhancement effect becomes saturated at higher values of A_p . From Eq. (6), we can see that the enhancement of Δλ _B / ΔT by increasing A_p is saturated when A_p • E_p becomes larger than A_f • E_f . Our results and the analytic solution show that the temperature sensitivity of the FBG can be effectively enhanced only with thin layer of the PDMS jacket. In addition, we can use A_p as a device design parameter to control the temperature sensitivity of the FBG sensor. It is also expected that the chirp-shaped spectra under temperature variation can be easily tailored by using the PDMS jacket with A_p variation along the fiber axis direction. Previously, we have shown that the selective chemical sensing is available with the PDMS-coated FBG structure by using the selective swelling effect of the PDMS under chemical exposure [15] . The previous analytic model, derived for the selective chemical sensing, can be improved with this work. We proposed a highly temperature-sensitive FBG structure,where the bare FBG was coated with the elastomeric PDMS jacket layer. The analytic model was also derived, which matched well with the experi-mental results. The experimental results as well as the theoretical model showed that the amount of the tensile force onto the PDMS-coated FBG, induced by temperature variation, was highly dependent on the cross-section area of the PDMS jacket, which means that we can use our structure for enhancing temperature sensitivity effectively or for tailoring temperature-dependent spectral shape change for several other sensing appli-cations with modified PDMS shapes. The proposed PDMS-coated FBG sensor is expected to be widely used for various applications due to its high temperature sensitivity, easy fabri-cation,high durability and stability without interfacial residual stress between the PDMS and the fiber.