Anti-radiation global optical system

Abstract

The application discloses an anti-radiation global plane optical system, which is sequentially provided with a first lens, a second lens, a third lens, a fourth lens, a fifth lens, a sixth lens, a seventh lens, an eighth lens, a ninth lens and a narrow-band filter along an axial direction from an object side to an image side; the first lens, the third lens, the fourth lens, the fifth lens, the seventh lens and the eighth lens are lenses with positive focal lengths; the second lens, the sixth lens and the ninth lens are lenses with negative focal lengths; an object side surface of the fourth lens is provided as an aperture stop of the system; the application can effectively inhibit the generation of radiation color centers, realizes deep compensation of wide-band chromatic aberration and field curvature without depending on aspheric surfaces and heavy shielding layers, guarantees light weight and low-cost processing of the system, and obtains high-resolution and low-distortion imaging effects.

Description

Technical Field

[0001] This invention relates to the fields of optical design and optical imaging technology, and in particular to a radiation-resistant global surface optical system. Background Technology

[0002] With the rapid development of aerospace remote sensing, deep space exploration, and other fields, the stability and service life of optical systems in orbit have become key factors restricting the conduct of space missions. Existing space optical systems mostly use conventional optical glass materials. While these materials can meet imaging requirements in terrestrial environments, they are prone to ionization and the formation of color centers in the high-energy cosmic ray radiation environment of space. This leads to a significant decrease in the glass's spectral transmittance and a continuous degradation of optical performance, severely affecting the imaging quality of the optical system and drastically shortening the spacecraft's in-orbit service life.

[0003] To mitigate performance degradation caused by radiation, traditional technologies often employ the addition of external shielding layers or protective covers. These solutions not only significantly increase the overall weight and manufacturing cost of the optical system but also raise the risk of system failure due to the introduction of additional moving parts, making them unsuitable for the lightweight and high-reliability requirements of space missions. Other optical systems have achieved effective aberration correction through optimized lens structures, but the materials used have not undergone radiation-resistant screening, failing to address the problem of space radiation damage at its source. Furthermore, some systems utilize aspherical lens designs, which are difficult to manufacture, highly tolerance-sensitive, and have low yield rates, further increasing production and maintenance costs.

[0004] Currently, space optical systems that combine radiation resistance, low-cost fabrication, and excellent imaging performance are still relatively scarce, making it difficult to meet the practical needs of long-term spaceborne remote sensing and deep space exploration missions. Therefore, this invention designs an optical system entirely constructed using radiation-resistant glass. The glass materials used have been selected through radiation experiments and exhibit excellent radiation resistance stability, significantly reducing the impact of cosmic rays on the optical path and maintaining their initial optical properties over a long period. This solution effectively extends the system's lifespan without requiring additional shielding structures, achieving a balance between lightweight design and high reliability, making it particularly suitable for long-term spaceborne missions. Summary of the Invention

[0005] This application provides a radiation-resistant global surface optical system, solving the technical problem that existing optical systems are prone to color centers under cosmic ray irradiation, leading to decreased spectral transmittance and optical performance degradation, thus restricting the long-term reliable operation of aerospace optical systems. Through the structural and material property design of the global surface optical system, the system maintains stable initial optical performance during long-term space missions without the need for additional shielding structures. At the same time, the global surface lens design reduces processing difficulty and cost, and through reasonable power distribution and dispersive material matching, it effectively eliminates chromatic aberration and higher aberrations, achieving excellent imaging across a wide band of confocal surfaces, while balancing system lightweight, high reliability, and high imaging quality.

[0006] This application provides a radiation-resistant global surface optical system. The optical system is provided with a first lens (1), a second lens (2), a third lens (3), a fourth lens (4), a fifth lens (5), a sixth lens (6), a seventh lens (7), an eighth lens (8), a ninth lens (9), a narrowband filter (10), and an image plane (11) arranged sequentially along the object-to-image axial direction. All optical surfaces of the first lens (1), the second lens (2), the third lens (3), the fourth lens (4), the fifth lens (5), the sixth lens (6), the seventh lens (7), the eighth lens (8), and the ninth lens (9) are spherical. The first lens (1), the third lens (3), the fourth lens (4), the fifth lens (5), the seventh lens (7), and the eighth lens (8) are all lenses with positive optical power. The second lens (2), the sixth lens (6), and the ninth lens (9) are all lenses with negative optical power. The object side of the fourth lens (4) is set as the aperture stop of the system.

[0007] Preferably, the Abbe numbers Vd1, Vd3, Vd5, Vd8, and Vd9 of the materials of the first lens (1), the third lens (3), the fifth lens (5), the eighth lens (8), and the ninth lens (9) satisfy: Vd1≥70; Vd3≥70; Vd5≥70; Vd8≥70; Vd9≥70; The Abbe number Vd2 of the material of the second lens (2) satisfies: Vd2≥40; The Abbe numbers Vd4 and Vd7 of the materials of the fourth lens (4) and the seventh lens (7) satisfy: Vd4≥20; Vd7≥20; The Abbe number Vd6 of the material of the sixth lens (6) satisfies: 20≤Vd6≤50.

[0008] Preferably, the absolute values ​​of the differences in the Abbe numbers Vd3, Vd4, Vd5, and Vd6 of the materials of the third lens (3), the fourth lens (4), the fifth lens (5), and the sixth lens satisfy the following relationship: |Vd5−Vd6|≥30;|Vd3−Vd4|≥30;

[0009] Preferably, the Abbe numbers Vd3 and Vd4 of the materials of the third lens (3) and the fourth lens (4) further satisfy: |Vd3−Vd4|≥65.

[0010] Preferably, the effective focal lengths of the first lens (1) to the ninth lens (9) are respectively denoted as: to The total focal length of the optical system is denoted as . The ratio of the effective focal length of each lens to the total focal length satisfies the following constraints: .

[0011] Preferably, the fourth lens (4) is provided with the aperture stop STO of the optical system on the first surface facing the object.

[0012] Preferably, the first lens (1), the third lens (3), the fifth lens (5) and the eighth lens (8) are made of CAF2 material.

[0013] Preferably, a narrowband filter (10) is disposed between the ninth lens (9) and the image plane (11).

[0014] One or more technical solutions provided in the embodiments of this application have at least the following technical effects or advantages: 1. The nine lenses used in this application all have spherical surfaces. Through precise matching of curvature radii and optimized thickness combination, aberration correction is achieved without introducing aspherical surfaces. This solves the problems of high cost and excessive tolerance sensitivity of aspherical lenses in CNC polishing and ion beam shaping processes, and avoids the stringent requirements of assembly tilt and eccentricity for complex surface shapes. Manufacturing can be completed using conventional high-precision spherical grinding processes, improving production efficiency and product consistency, reducing technical risks and manufacturing costs, while enhancing the system's tolerance to assembly tolerances, providing a highly reliable and low-cost optical payload solution for space exploration missions.

[0015] 2. This application strictly limits the normalized focal length ratio of each lens to a specific range to prevent the introduction of advanced aberrations due to excessive focal length of a single lens, thereby achieving an effective balance of system aberrations. While ensuring imaging quality, the total length is controlled within 250mm, taking into account both compactness and high performance.

[0016] 3. This application utilizes a combination of high Abbe number (Vd≥70) and low Abbe number materials, and the difference in Abbe number between key lens pairs is ≥30, to achieve efficient correction of axial chromatic aberration and magnification chromatic aberration, thereby achieving multispectral confocal imaging.

[0017] 4. The large Abbe number difference formed by the third and fourth lenses of this application, combined with a specific optical power allocation, significantly improves secondary spectral residuals and enhances the registration accuracy and image consistency of multi-band imaging. The fifth and sixth lenses of this application adopt an alternating negative and positive optical power separation structure, combined with an air gap design, to effectively correct higher-order terms of spherical aberration and optimize image plane flatness, while also facilitating back intercept compression. The seventh to ninth lenses of this application adopt a positive-positive-negative optical power sequence to centrally compensate for residual field curvature and distortion, keeping the full field-of-view distortion within 0.21% and ensuring the geometric fidelity of remote sensing images.

[0018] 5. A narrowband filter is set between the ninth lens and the image plane, integrating the mechanical matching of different bandwidths of the front-end narrowband filter and the focal plane fine adjustment, so as to achieve zero focal plane drift when switching between different bands and improve the data synchronization and imaging consistency of multispectral continuous observation. Attached Figure Description

[0019] Figure 1 This is a schematic diagram of the optical system of the present invention; Figure 2 This is a diagram showing the lens parameters of the optical system of the present invention; Figure 3 This is a schematic diagram of the irradiation test curve of the radiation-resistant glass used in the optical system of the present invention; Figure 4 This is a schematic diagram of the Seidel aberration in the optical system of the present invention; Figure 5 This is a diffraction MTF curve of the optical system of the present invention; Figure 6 This is a dot diagram of the optical system of the present invention; Figure 7 The field curvature and distortion diagrams of the optical system of this invention are shown. Figure 8 This is the FFT diffraction circle energy map of the present invention; Figure 9 This is a light aberration diagram of the present invention; In the diagram: 1. First lens; 2. Second lens; 3. Third lens; 4. Fourth lens; 5. Fifth lens; 6. Sixth lens; 7. Seventh lens; 8. Eighth lens; 9. Ninth lens; 10. Narrowband filter; 11. Image plane. Detailed Implementation

[0020] This application provides a radiation-resistant global surface optical system, which solves the technical problem that conventional optical systems in the prior art are prone to color centers under space cosmic ray irradiation, resulting in decreased spectral transmittance and optical performance degradation, thus restricting the reliable operation of aerospace optical systems for a long time.

[0021] This application addresses the radiation damage problem by improving the lens material and structure. Without requiring additional shielding, it significantly reduces the impact of cosmic rays on the optical path, ensuring that the optical system maintains stable initial performance during long-term space missions, while also balancing lightweight design and high reliability.

[0022] To better understand the above technical solutions, the following will provide a detailed explanation of the technical solutions in conjunction with the accompanying drawings and specific implementation methods.

[0023] like Figure 1 As shown, this application discloses a radiation-resistant global surface optical system. The optical system is a transmission optical system with a coaxial structure. Along the incident direction of light, it consists of a first lens 1, a second lens 2, a third lens 3, a fourth lens 4, a fifth lens 5, a sixth lens 6, a seventh lens 7, an eighth lens 8, and a ninth lens 9. After being refracted sequentially by the above lenses, the light passes through a narrow-band filter 10 and finally enters the image plane 11. The lens surfaces of the optical system are all spherical, and all lens materials are radiation-resistant glass that has been tested and selected through radiation experiments. The narrow-band filter 10 is disposed between the ninth lens 9 and the image plane 11.

[0024] The first lens 1 sequentially passes through the second lens 2, the third lens 3, the fourth lens 4, the fifth lens 5, the sixth lens 6, the seventh lens 7, the eighth lens 8, and the ninth lens 9. After passing through the narrow-band filter 10, the light is further subdivided into different wavelength bands and imaged onto the image plane 11. The second lens 2, the third lens 3, the fourth lens 4, the fifth lens 5, and the sixth lens 6 primarily function to aberrate chromatic aberration and correct principal aberrations, while the seventh lens 7, the eighth lens 8, and the ninth lens 9 primarily function to converge light and also compensate for residual aberrations. Through the cross-arrangement and combination of high Abbe number and low Abbe number lenses from the first to the ninth lens, the optical power of this optical system is effectively balanced, and the chromatic aberration of the optical system is corrected.

[0025] The system operates over a wide spectral range from 0.4 μm to 0.88 μm, with an entrance pupil diameter of 50 mm, a total focal length of 156 mm, a relative aperture F-number of 3.2, and a diagonal half-field of view of 8.5 degrees. The total optical length of the system is 250 mm; the center field of view MTF ≥ 0.6 (134 lp / mm), the edge field of view MTF ≥ 0.5 (134 lp / mm); and the total field of view distortion is < 0.21%, achieving a balance between compact structure and high-performance imaging.

[0026] like Figure 2 As shown, the first lens 1 is a positive power lens made of CAF2 material. This material has a refractive index (Nd) of 1.43 and an Abbe number of 95.00. In its specific structural parameters, the object-side surface S1 of the first lens 1 has a radius of curvature of 135.94 mm, the image-side surface S2 has a radius of curvature of 1605.89 mm, and a center thickness of 9.76 mm. The first lens 1 is the primary lens in the system, undertaking most of the beam collection work. Its high Abbe number ensures minimal primary chromatic aberration under large-aperture incident conditions. Simultaneously, its large image-side surface radius of curvature reduces the deflection angle of rays at the edge of the field of view.

[0027] The second lens 2 is a negative optical power lens, made of BAK7G material with a refractive index of 1.57 and an Abbe number of 56.11. The second lens 2 maintains a 7.54 mm gap from the first lens 1. The object-side surface S3 radius of curvature of the second lens 2 is -146.22 mm, the image-side surface S4 radius of curvature is 2228.75 mm, and the center thickness is 7.0 mm. The negative optical power of the second lens 2 compensates for the positive optical power of the first lens 1, primarily used to correct the spherical aberration of the front group of the system.

[0028] The third lens 3 is a positive power lens made of CAF2 material. A 3.0mm gap is maintained between the third lens 3 and the second lens 2. Its object-side surface (S5) has a radius of curvature of 134.05mm, its image-side surface (S6) has a radius of curvature of 444.66mm, and its thickness is 8.0mm. The third lens 3 further converges the light beam through its positive power and works in conjunction with subsequent lenses to compensate for dispersion.

[0029] The fourth lens 4 is a positive power lens, made of N-SF14G material with a refractive index of 1.76 and an Abbe number of 26.53. The object-side surface S7 of the fourth lens 4 is defined as the system's aperture stop STO. Its object-side surface S7 has a radius of curvature of -526.14 mm, its image-side surface S8 has a radius of curvature of -207.33 mm, and its thickness is 7.0 mm. The air gap between the fourth lens 4 and the third lens 3 is 51.9 mm. Since the Abbe number of the third lens 3 is 95.00, while the Abbe number of the fourth lens 4 is 26.53, the absolute value of the difference in Abbe numbers between the two reaches 68.47, far exceeding the constraint threshold of 30. This strong combination of dispersion gradients achieves depth correction of the second-order spectrum, eliminating residual chromatic aberration in broadband imaging.

[0030] The fifth lens 5 is a positive power lens made of CAF2 material, with an object-side radius S9 of 157.21 mm, an image-side radius S10 of -926.64 mm, and a thickness of 8.0 mm. The fifth lens 5 is spaced 3.0 mm from the fourth lens 4.

[0031] The sixth lens 6 is a negative power lens, made of N-KZF55 material with a refractive index of 1.65 and an Abbe number of 39.70. The object-side surface S11 of the sixth lens 6 has a radius of -342.64 mm, the image-side surface S12 has a radius of 81.42 mm, and a thickness of 8.0 mm. The absolute value of the Abbe number difference between the fifth lens 5 and the sixth lens 6 is 55.3, also satisfying the design constraint of greater than 30. This alternating positive and negative power distribution, combined with air gaps, ensures the flatness of the image plane.

[0032] The seventh lens 7, the eighth lens 8, and the ninth lens 9 constitute the rear imaging group of the system.

[0033] The seventh lens 7 is positive power, made of CAF2 material, with S13 radius of 126.88mm, S14 radius of -225.19mm, and thickness of 10.17mm.

[0034] The eighth lens 8 is positive power, made of CAF2 material, with S15 radius of 58.96mm, S16 radius of 214.73mm, and thickness of 11.0mm.

[0035] The ninth lens has negative optical power, is made of SILICA material, has a refractive index of 1.46, an Abbe number of 67.82, an S17 radius of -45.52 mm, an S18 radius of -270.93 mm, and a thickness of 8.0 mm. The post-imaging group completes the final convergence of the light beam and reduces distortion across the entire field of view through a positive-positive-negative optical power sequence.

[0036] A narrowband filter 10 is positioned 17 mm behind the ninth lens 9. The substrate material of the narrowband filter 10 is 1 mm thick SILICA quartz glass, and a high-precision interference film is deposited on its surface. The narrowband filter 10 performs selective transmission of specific spectral bands, achieving high-purity multispectral imaging in conjunction with the front-end optical system. The light finally passes through the narrowband filter 10, passes through a 1 mm air gap, and then illuminates the image plane 11.

[0037] The operating principle and process of this optical system are as follows: In step S1, the light beam is first deflected by the first lens 1. Due to its positive optical power, the diverging or parallel light beam begins to converge toward the optical axis.

[0038] In step S2, the light beam passes sequentially through the aberration correction group consisting of the second lens 2 to the sixth lens 6. During this process, light of different wavelengths will have different deflection paths due to the dispersive properties of the glass material. The system utilizes the high Abbe number of CAF2 and the low Abbe number of N-SF14 and N-KZF55, and through multiple refraction compensation with positive and negative optical power, so that the axial chromatic aberration and magnification chromatic aberration of different colors of light are controlled within the diffraction limit range after passing through the sixth lens 6.

[0039] In step S3, the light beam enters the imaging convergence group composed of the seventh lens 7 to the ninth lens 9. This stage focuses on solving the problem of energy concentration at the edge of the field of view. Through the double concave design of the ninth lens 9, the exit pupil position is stretched, the angle of light incident on the image plane 11 is improved, and the cosine fourth power attenuation effect of the detector pixels is reduced.

[0040] In step S4, after the beam is split by the narrow-band filter 10, background stray light and non-target spectral bands are filtered out, and finally a clear image point with high contrast and low distortion is formed on the image plane 11.

[0041] In this embodiment, the optical power distribution among the lenses of this application achieves overall aberration balance and structural compactness of the system, specifically satisfying the following relationship: in, The total effective focal length of the system is given by the focal lengths of each lens in sequence. 、 、 、 、 、 、 、 、 The focal length of each lens relative to the system focal length The normalized value satisfies the following range: In the formula, For the system focal length, The focal length of the first lens 1 The focal length of the second lens 2 The focal length of the third lens 3 The focal length of the fourth lens 4. The focal length of the fifth lens 5. The focal length of the sixth lens 6. The focal length of the seventh lens 7. The focal length of the eighth lens 8. This is the focal length of the ninth lens, 9.

[0042] Along the direction of light incidence, the optical power and dispersion coefficient (Abbe number Vd) of each lens satisfy the following conditions: (1) The first lens has positive optical power and a dispersion coefficient Vd1≥70; (2) The second lens has negative optical power and is placed at an interval from the first lens, with a dispersion coefficient Vd2≥40; (3) The third lens has positive optical power and is placed at an interval from the second lens, with a dispersion coefficient Vd3≥70; (4) The fourth lens has positive optical power, and its first surface is the aperture of the optical system, used to limit the beam aperture. It is placed at an interval from the third lens, and its dispersion coefficient Vd4≥20, and satisfies |Vd3−Vd4|≥30. (5) The fifth lens has positive optical power and is placed at an interval from the fourth lens, with a dispersion coefficient Vd5≥70; (6) The sixth lens has negative optical power and is placed at an interval from the fifth lens. Its dispersion coefficient is 50≥Vd6≥20 and satisfies |Vd5−Vd6|≥30; (7) The seventh lens has positive optical power and is placed at an interval from the sixth lens. Its dispersion coefficient Vd7 ≥ 20. (8) The eighth lens has positive optical power and is placed alternately with the seventh lens. Its dispersion coefficient Vd8 ≥ 70. (9) The ninth lens has a negative optical power and is placed at an interval from the eighth lens. Its dispersion coefficient Vd9 ≥ 70.

[0043] The optical system uses glass as a material, such as... Figure 3 As shown, by selecting materials with low refractive index and high Abbe number and materials with high refractive index and low Abbe number and using them in combination, the optical power and chromatic aberration between systems can be balanced.

[0044] As shown in Figure 4, the aberrations of the optical system are compensated to near their minimum values ​​by the coordination of different lenses and surfaces, ensuring that the entire optical system has excellent and stable imaging performance.

[0045] like Figure 5 The figure shows the diffraction modulation transfer function (MTF) curves of this optical system in the 0.4 μm to 0.88 μm band. At the spatial cutoff frequency of 134 lp / mm, the MTF value is greater than 0.5 across the entire field of view. This result indicates that the system possesses near-diffraction-limited resolution across the entire operating band and field of view, meeting the requirements for high-resolution aerospace remote sensing imaging.

[0046] like Figure 6 The image shows the point plots of this optical system under various fields of view. At an 8.5° half-field angle, the field of view is close to the Airy radius, while the RMS radii of the point plots for the remaining fields of view are all smaller than the Airy radius. This indicates that the system achieves good geometric aberration correction in most fields of view, exhibits high energy concentration, and produces sharp images.

[0047] like Figure 7 The figure shows the field curvature and distortion curves of this optical system. The field curvature curves show that the meridional and sagittal field curvatures are both controlled within ±0.042 mm across the entire field of view, indicating excellent image plane flatness. The distortion curves show that the distortion curves for different wavelengths are highly consistent, and the maximum distortion value across the entire field of view is less than 0.202%. This level of distortion control has significant advantages for multispectral stitching and geometric measurement applications.

[0048] like Figure 8 The figure shows the ingress energy curve calculated based on FFT diffraction. Within a radius of 6 μm, the ingress energy fraction of the system is greater than 0.9. This result indicates that the system has excellent energy concentration capability, can effectively match small pixel-sized detectors, and improve the signal-to-noise ratio for weak signal detection.

[0049] like Figure 9As shown, the light aberration curves are displayed for different wavelengths in each field of view. The curves are generally symmetrical, with small fluctuations and good linearity, and no significant abrupt changes in higher-order aberrations are observed. This further verifies that the system achieves balanced correction of spherical aberration, coma, astigmatism, and chromatic aberration through a nine-piece global surface structure and radiation-resistant materials.

[0050] This system employs a combination of different dispersive materials for chromatic aberration reduction. Seven of the nine lenses are low-dispersion materials with an Abbe number greater than 50. In particular, the difference in Abbe number between any two lenses significantly reduces chromatic aberration; for example, the difference in Abbe number between the third lens (3) and the fourth lens (4) is ≥65; and the difference in Abbe number between the fourth lens (4) and the fifth lens (5) is ≥55. This method keeps chromatic aberration within a small range. Combined with the narrowband filter (10), it enables zero focal plane drift across different spectra in different fields of view, achieving excellent imaging results.

[0051] This system employs a spherical surface design. Compared to aspherical designs, spherical systems are less sensitive to assembly tolerances, exhibiting higher yield and consistency during mechanical parts processing and optical centering assembly. Through the rational allocation of optical power among nine lenses, this invention utilizes a spherical combination to replace the correction function of aspherical lenses. The system also incorporates thermal aberration mitigation design to address the thermal effects of the space environment. Since different materials have different refractive index temperature coefficients, materials with positive and negative temperature coefficients are selected for matching. When the ambient temperature fluctuates drastically, the changes in the lens curvature radius and refractive index cancel each other out in the optical path, thus maintaining the stability of the focal plane position and avoiding image blurring caused by temperature changes. This invention provides a radiation-resistant global surface optical system that suppresses color center effects through the selection of fully radiation-resistant materials and corrects aberrations across the entire wavelength range through the precise layout of the nine-element global surface structure, achieving a comprehensive goal of long lifespan, lightweight design, and high-resolution imaging without the need for a physical shield.

[0052] The embodiments described herein are preferred embodiments of the present invention and are not intended to limit the scope of protection of the present invention. Therefore, all equivalent changes made to the structure, shape, and principle of the present invention should be covered within the scope of protection of the present invention. Although preferred embodiments of the present invention have been described, those skilled in the art, once they understand the basic inventive concept, can make other changes and modifications to these embodiments. Therefore, the appended claims are intended to be interpreted as including the preferred embodiments as well as all changes and modifications falling within the scope of the present invention. Obviously, those skilled in the art can make various modifications and variations to the present invention without departing from the spirit and scope of the present invention. Thus, if these modifications and variations of the present invention fall within the scope of the claims of the present invention and their equivalents, the present invention also intends to include these modifications and variations.

Claims

1. A radiation-resistant global surface optical system, characterized in that, The optical system is provided with a first lens (1), a second lens (2), a third lens (3), a fourth lens (4), a fifth lens (5), a sixth lens (6), a seventh lens (7), an eighth lens (8), a ninth lens (9), a narrowband filter (10), and an image plane (11) in sequence along the object-to-image axial direction. All optical surfaces of the first lens (1), the second lens (2), the third lens (3), the fourth lens (4), the fifth lens (5), the sixth lens (6), the seventh lens (7), the eighth lens (8), and the ninth lens (9) are spherical. The first lens (1), the third lens (3), the fourth lens (4), the fifth lens (5), the seventh lens (7), and the eighth lens (8) are all lenses with positive optical power. The second lens (2), the sixth lens (6), and the ninth lens (9) are all lenses with negative optical power. The object side of the fourth lens (4) is set as the aperture stop of the system.

2. The radiation-resistant global surface optical system as described in claim 1, characterized in that, The Abbe numbers Vd1, Vd3, Vd5, Vd8, and Vd9 of the materials of the first lens (1), the third lens (3), the fifth lens (5), the eighth lens (8), and the ninth lens (9) satisfy: Vd1≥70; Vd3≥70; Vd5≥70; Vd8≥70; Vd9≥70; The Abbe number Vd2 of the material of the second lens (2) satisfies: Vd2≥40; The Abbe numbers Vd4 and Vd7 of the materials of the fourth lens (4) and the seventh lens (7) satisfy: Vd4≥20; Vd7≥20; The Abbe number Vd6 of the material of the sixth lens (6) satisfies: 20≤Vd6≤50.

3. The radiation-resistant global surface optical system as described in claim 2, characterized in that, The absolute values ​​of the differences in the Abbe numbers Vd3, Vd4, Vd5, and Vd6 of the materials of the third lens (3), the fourth lens (4), the fifth lens (5), and the sixth lens satisfy the following relationship: |Vd5−Vd6|≥30;|Vd3−Vd4|≥30; 4. The radiation-resistant global surface optical system as described in claim 3, characterized in that, The Abbe numbers Vd3 and Vd4 of the materials of the third lens (3) and the fourth lens (4) further satisfy: |Vd3−Vd4|≥65.

5. The radiation-resistant global surface optical system as described in claim 1, characterized in that, The effective focal lengths of the first lens (1) to the ninth lens (9) are respectively denoted as: to The total focal length of the optical system is denoted as . The ratio of the effective focal length of each lens to the total focal length satisfies the following constraints: 。 6. The radiation-resistant global surface optical system as described in claim 1, characterized in that, The fourth lens (4) is provided with the aperture stop STO of the optical system on the first surface facing the object.

7. The radiation-resistant global surface optical system as described in claim 1, characterized in that, The first lens (1), the third lens (3), the fifth lens (5) and the eighth lens (8) are made of CAF2 material.

8. The radiation-resistant global surface optical system as described in claim 1, characterized in that, A narrowband filter (10) is disposed between the ninth lens (9) and the image plane (11).

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